FIBEROPTIC SENSOR TECHNOLOGY HANDBOOK
FIBEROPTIC SENSOR TECHNOLOGY HANDBOOK
FIBEROPTIC SENSOR TECHNOLOGY HANDBOOK
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<strong>FIBEROPTIC</strong> <strong>SENSOR</strong><br />
<strong>TECHNOLOGY</strong> <strong>HANDBOOK</strong><br />
by<br />
Charles M. Davis<br />
Edward F. Carome<br />
Martin H. Weik<br />
Shaoul Ezekiel<br />
Robert E. Einzig<br />
Publisher and Distributor<br />
Optical Technologies (OPTECH)<br />
A Division of Dynamic Systems, Inc.<br />
360 Herndon Parkway, Suite 1200<br />
Herndon, VA 22070-5225<br />
Tel: (703) 478-0844 Fax: (703) 478-0649
Copyright Optical Technologies, Inc., 1982; 1986<br />
Registration Number TX 1-094-758<br />
All rights reserved.<br />
No part of this publication may be<br />
reproduced, copied or transmitted, in any<br />
form or by any means - graphic, electronic,<br />
or mechanical, including photocopying,<br />
taping or information storage and retrieval<br />
systems - without the prior written<br />
permission of Optical Technologies (OpTECH).
FOREWORD<br />
THE <strong>FIBEROPTIC</strong> <strong>SENSOR</strong> <strong>TECHNOLOGY</strong> <strong>HANDBOOK</strong><br />
The <strong>FIBEROPTIC</strong> <strong>SENSOR</strong> <strong>TECHNOLOGY</strong> <strong>HANDBOOK</strong> reflects<br />
the latest technology concerning the field of<br />
fiberoptic in general and fiberoptic sensors in<br />
particular. The fiberoptic sensor technology principles<br />
and practices laid down in this <strong>HANDBOOK</strong> will give the<br />
reader a solid basis for mastering a relatively new<br />
technology. Only a nominal general technical background<br />
is needed to fully comprehend its contents. The<br />
contributing authors have been as explicit and rigorous<br />
in their presentation as time and space constraints in<br />
this <strong>HANDBOOK</strong> would permit. All the material has been<br />
edited to ensure coherency and consistency.<br />
OPTICAL TECHNOLOGIES, INC.<br />
Optical Technologies, Inc. (OPTECH) is a young and<br />
rapidly growing corporation devoted to the research and<br />
development of useful fiberoptic sensor applications and<br />
to the advancement of fiberoptic sensor technology.<br />
OPTECH is recognized as a leader in this field. The cofounders<br />
of OPTECH, Dr. Charles M. Davis and Mr. Robert<br />
E. Einzig, who are also authors of this <strong>HANDBOOK</strong>, are<br />
pioneers in the field of fiberoptic sensor technology.<br />
Dr. Davis headed the branch at the Naval Research<br />
Laboratory that designed and produced the first<br />
fiberoptic hydrophore. He has since collaborated in the<br />
design of numerous other fiberoptic sensor systems. Mr.<br />
Einzig has also designed fiberoptic sensor systems for<br />
private research laboratories, industry and government.<br />
Finally, both men were the key contributors to the<br />
development of the Navy’s Fiber Optic Sensor System<br />
(FOSS) Program in 1977. Presently, their experience and<br />
talents are being applied at OPTECH where, together with<br />
other physicists and engineers specializing in<br />
fiberoptic sensing, advances in the field are continuing<br />
to be made. To date, OPTECH’S experience with<br />
fiberoptic sensors includes development of sensors for<br />
the measurement of temperature, pressure, acoustic<br />
signals, acceleration, magnetic fields, and seismic<br />
disturbances.<br />
AUTHORS<br />
Charles M. Davis, PhD. Currently Dr. Davis is Vice<br />
President of Optical Technologies, Inc. He has over 30<br />
years of experience in acoustooptics and physical<br />
acoustics. As head of the Physical Acoustics Branch at<br />
the Naval Research Laboratory, he was instrumental in<br />
the development of the fiberoptic hydrophore and the<br />
establishment of the FOSS Program.<br />
Edward F. Carome, PhD. Currently Dr. Carome is a<br />
Professor of Physics at John Carroll University. He<br />
participated in the initial research at the Naval<br />
Research Laboratory that led to the development of the<br />
fiberoptic hydrophore.<br />
Martin H. Weik, D.SC. Currently Dr. Weik is a<br />
senior systems analyst at Dynamic Systems, Inc. Dr.<br />
Weik has written several comprehensive dictionaries in<br />
the fields of computers, information processing systems,<br />
fiberoptic, lightwave propagation, and general<br />
communications.<br />
Shaoul Ezekiel, D.SC. Currently Dr. Ezekiel is a<br />
Professor at MIT. He has conducted research concerned<br />
with ultraprecision measurements using optical<br />
techniques. More recently, he has investigated the use<br />
of passive resonators and fiberoptic interferometers for<br />
rotation measurements.<br />
Robert E. EinziR, MSEE. Currently Mr. Einzig<br />
serves as President of Optical Technologies, Inc. He<br />
has extensive applications experience in fiberoptic<br />
sensors and data transmission systems, which adds to his<br />
broad underwater acoustic sensor background.<br />
ACKNOWLEDGEMENT<br />
Appreciation is extended to Dynamic Systems,Inc.<br />
and specifically to Mickey Hedrick, Sandee M. Boyer, and<br />
Sue M. Gift, and their supporting staff for their<br />
secretarial, word-processing, and graphics support in<br />
the preparation of this Handbook.<br />
Robert E. Einzig<br />
President<br />
Optical Technologies, Inc.
TABLE OF CONTENTS<br />
FOREWORD<br />
CHAPTER<br />
1.0<br />
1.1<br />
1.2<br />
INTRODUCTION<br />
Background .<br />
Purpose . .<br />
. . . . . . . . . . . . . . . . . . . . . . . . . . . .1-1<br />
. . . . . . . . . . . . . . . . . . . . . . . . . . . .1-1<br />
. . . . . . . . . . . . . . . . . . . . . . . . . . . .1-1<br />
1.3<br />
Contents by Chapter . . . . . . . . . . . . . . . . . . . . . . . .1-1<br />
2.0<br />
2.1<br />
2.2<br />
<strong>FIBEROPTIC</strong> <strong>SENSOR</strong> COMPONENTS . . . . . . . . . . . . . . . . . . . .2-1<br />
Optical Fiber Properties . . . . . . . . . . . . . . . . . . . . . .2-1<br />
2.1.1 Design Objectives . . . . . . . . . . . . . . . . . . . . . .2-1<br />
2.1.2 Lightwave Propagation . . . . . . . . . . . . . . . . . . . .2-4<br />
2.1.3 Propagation Modes . . . . . . . . . . . . . . . . . . . . . .2-5<br />
Optical Fiber Fabrication . . . . . . . . . . . . . . . . . . . . .2-12<br />
2:2.1<br />
2.2.2<br />
Refractive Index Profile Control . . . . . . . . . . . . . .2-12<br />
Fiber Fabrication Processes . . . . . . . . . . . . . . . . .2-13<br />
2.2.2.1 The Double-Crucible Process. . . . . . . . . . . . .2-13<br />
2.2.2.2 The Inside Vapor-Phase Oxidation (IVPD) Process . .2-14<br />
2.2.2.3 The Outside Vapor-Phase Oxidation (OVPD) Process . .2-15<br />
2.2.2.4 The Vapor Axial Deposition (VAD) Process . . . . . .2-15<br />
2.2.3 Fiber Strength . . . . . . . . . . . . . . . . . . . . . . .2-16<br />
2.3<br />
2.4<br />
Solid State Fiberoptic Light Sources . . . . . . . . . . . . . . .<br />
2.3.1 Energy Levels in Semiconductors . . . . . . . . . . . . . .<br />
2.3.2 Light Emitting Diodes (LEDs) and Diode Laaers . . . . . . .<br />
Photodetector . . . . . . . . . . . . . . . . . . . . . . . . . .<br />
.2-17<br />
.2-17<br />
.2-19<br />
.2-22<br />
3.0<br />
3.1<br />
3.2<br />
3.3<br />
4.0<br />
<strong>FIBEROPTIC</strong> COMPONENT INTERCONNECTION . . . . . . . . . . . . . . .<br />
Fiberoptic Connectors and Splices . . . . . . . . . . . . . . . .<br />
3.1.1 References. . . . . . . . . . . . . . . . . . . . . . . . .<br />
Fiberoptic Couplers . . . . . . . . . . . . . . . . . . . . . . .<br />
3.2.1 References . . . . . . . . . . . . . . . . . . . . . . . .<br />
Fiberoptic Cables . . . . . . . . . . . . . . . . . . . . . . . .<br />
3.3.1 General . . . . . . . . . . . . . . . . . . . . . . . . . .<br />
3.3.2 Commercial Fiberoptic Cables. . . . . . . . . . . . . . . .<br />
3.3.3 Summary . . . . . . . . . . . . . . . . . . . . . . . . . .<br />
LICRTWAVES IN <strong>FIBEROPTIC</strong> <strong>SENSOR</strong>S . . . . . . . . . . . . . . . . .<br />
.3-1<br />
.3-1<br />
.3-5<br />
.3-5<br />
.3-7<br />
.3-7<br />
.3-7<br />
.3-8<br />
.3-8<br />
.4-1<br />
4.1<br />
Interferometric Fiberoptic Sensors . . . . . . . . . . . . . . . .<br />
4.1.1 Intensity Interferometry . . . . . . . . . . . . . . . . .<br />
4.1.1.1 Basic Principles . . . . . . . . . . . . . . . . .<br />
4.1.1.2 The Michelsen Interferometer . . . . . . . . . . .<br />
4.1.1.3 The Mach-Zehnder Interferometer . . . . . . . . .<br />
4.1.1.4 The Sagnac Interferometer . . . . . . . . . . . .<br />
4.1.1.5 The Fabry-Perot Interferometer . . . . . . . . . .<br />
4.1.1.6 Interferometer Sensitivity . . . . . . . . . . . .<br />
4.1.2 Fiberoptic Intensity Interferometers . . . . . . . . . . .<br />
4.1.3 Polarization in Fiberoptic Sensors . . . . . . . . . . . .<br />
.4-1<br />
.4-1<br />
.4-1<br />
.4-1<br />
.4-1<br />
.4-2<br />
.4-2<br />
.4-2<br />
.4-3<br />
.4-3
4.2 Phase<br />
4.2.1<br />
4.2.2<br />
4.2.3<br />
4.2.4<br />
4.2.5<br />
4.2.6<br />
4.2.7<br />
4.2.8<br />
and Intensity Detection . . . . . . . .<br />
Phase Detection . . . . . . . . . . . .<br />
Homodyne Detection Applications . . . .<br />
Phase Noise . . . . . . . . . . . . . .<br />
Amplitude Noise . . . . . . . . . . . .<br />
Satellite Modes and Multimode Operation<br />
Phase-Locked-Loop Operation . . . . . .<br />
Heterodyne Detection . . . . . . . . .<br />
References . . . . . . . . . . . . . .<br />
. . . . . . . . . .<br />
. . . . . . . . . .<br />
. . . . . . . . . .<br />
. . . . . . . . . .<br />
. . . . . . . . . .<br />
. . . . . . . . . .<br />
. . . . . . . . . .<br />
. . . . . . . . . .<br />
. . . . . . . . . .<br />
.4-5<br />
.4-5<br />
.4-8<br />
.4-8<br />
.4-9<br />
.4-9<br />
.4-1o<br />
.4-1o<br />
.4-11<br />
4.3 Integrated Optical Circuits (IOCS) . . . . . . . . . . . . . . . . .4-12<br />
5.0 <strong>FIBEROPTIC</strong> <strong>SENSOR</strong>S AND COMPONENTS . . . . . . . . . . . . . . . . .5-1<br />
5.1 Phase Modulated Fiberoptic Sensors . . . . . . . . . . . . . . . . .5-1<br />
5.1.1 General . . . . . . . . . . . . . . . . . . . . . . . . . . .5-1<br />
5.1.2 Fiberoptic Acoustic Sensors . . . . . . . . . . . . . . . . .5-2<br />
5.1.2.1 Acoustic Pressure Sensors . . . . . . . . . . . . .5-2<br />
5.1.2.2 Pressure Gradient Sensors . . . . . . . . . . . . .5-3<br />
5.1.3 Fiberoptic Magnetic Sensors . . . . . . . . . . . . . . . . .5-5<br />
5.1.4 Fiberoptic Electric Current Senaors . . . . . . . . . . . . .5-6<br />
5.1.5 Fiberoptic Spectrophones . . . . . . . . . . . . . . . . . .5-6<br />
5.1.6 Summary . . . . . . . . . . . . . . . . . . . . . . . . . . .5-7<br />
5.1.7 Reference . . . . . . . . . . . . . . . . . . . . . . . . .5-7<br />
5.2 Intensity Modulated Fiberoptic Sensors . . . . . . . . . . . . . . .5-7<br />
5.2.1 General . . . . . . . . . . . . . . . . . . . . . . . . . . .5-7<br />
5.2.2 Evanescent-Field Fiberoptic Sensor . . . . . . . . . . . . .5-8<br />
5.2.3 Reflection Coefficient Fiberoptic Sensor . . . . . . . . . .5-8<br />
5.2.4 Moving Grating Fiberoptic Sensor . . . . . . . . . . . . . .5-8<br />
5.2.5 Microbend Fiberoptic Sensor . . . . . . . . . . . . . . . . .5-9<br />
5.2.6 References . . . . . . . . . . . . . . . . . . . . . . . . .5-12<br />
5.3 Fiberoptic Linear Accelerometers . . . . . . . . . . . . . . . . . .5-12<br />
5.3.1 References. . . . . . . . . . . . . . . . . . . . . . . . . .5-14<br />
5.4 Fiberoptic Rotation-Rate Sensors . . . . . . . . . . . .<br />
5.4.1 Introduction. . . . . . . . . . . . . . . . . . .<br />
5.4.2 Methods of Rotation Sensing . . . . . . . . . . .<br />
5.4.3 Interest in Optical Rotation Sensors. . . . . . .<br />
5.4.4 Sagnac Effect in a Vacuum . . . . . . . . . . . .<br />
5.4.5 Sagnac Effect in a Medium . . . . . . . . . . . .<br />
5.4.6 The Magnitude of the Sagnac Effect. . . . . . . .<br />
5.4.7 Methods of Optical Rotation Sensing . . . . . . .<br />
5.4.8 Fundamental Limits in Optical Rotation Sensors. .<br />
5.4.9 Fiberoptic Rotation-Rate Sensors. . . . . . . . .<br />
5.4.10 Photon Shot-Noise Limit . . . . . . . . . . . . .<br />
5.4.11 Ideal Performance . . . . . . . . . . . . . . . .<br />
5.4.12 Measurement of Nonreciprocal Phase Shift. . . . .<br />
5.4.13 Methods of Nonreciprocal Phase Modulation . . . .<br />
5.4.14 Open Loop and Closed Loop Operation . . . . . . .<br />
5.4.15 Problems in Fiberoptic Rotation Sensors . . . . .<br />
5.4.16 Integrated Fiber “Gyros”. . . . . . . . . . . . .<br />
5.4.17 Fiber Gyro Performance. . . . . . . . . . . . . .<br />
5.4.18 Summary of Rotation-Rate Sensors. . . . . . . . .<br />
5.4.19 General Conclusions Regarding Fiberoptic Sensors.<br />
5.4.20References. . . . . . . . . . . . . . . . . . . .<br />
. . . . . .5-14<br />
. . . . . .5-14<br />
. . . . . .5-14<br />
. . . . . .5-15<br />
. . . . . .5-15<br />
. . . . . .5-16<br />
. . . . . .5-16<br />
. . . . . .5-16<br />
. . . . . .5-17<br />
. . . . . .5-18<br />
. . . . . .5-18<br />
. . . . . .5-19<br />
. . . . . .5-19<br />
. . . . . .5-20<br />
. . . . . .5-21<br />
. . . . . .5-21<br />
. . . . . .5-22<br />
. . . . . .5-23<br />
. . . . . .5-23<br />
. . . . . .5-23<br />
. . . . . .5-23<br />
6.0 <strong>FIBEROPTIC</strong> <strong>SENSOR</strong> ARRAYS AND TELEMETRY SYSTBMS . . . . . . . . . . .6-1<br />
6.1 Fiberoptic Sensor ArraYs . . . . . . . . . ● . . . . . . . . . . . .6-1<br />
6.1.1 Fiberoptic Senaor Array Design Considerations . . . . . . . .6-1<br />
6.1.1.1 General Design Considerations . . . . . . . . . . .6-1<br />
6.1.1.2 Specific Design Considerations . . . . . . . . . . .6-1<br />
6.1.2 Fiberoptic Sensor Array Basic Configurations . . . . . . . .6-1<br />
6.1.3 Fiberoptic Sensor Array Budgets . . . . . . . . . . . . . . .6-5
6.2 Fiberoptic Telemetry Systems . . . . . . . . . . . . . . .<br />
6.2.1 Fiberoptic Telemetry System Design Options . . . .<br />
6.2.2 Fiberoptic Telemetry System Basic Configurations .<br />
6.2.3 Telemetry System Budgets . . . . . . . . . . . . .<br />
6.2.3.1 Risetime Budget Analysis . . . . . . . . .<br />
6.2.3.2 Optical Power Budget Analysis . . . . . .<br />
6.2.3.3 Cost Budget Analysis . . . . . . . . . . .<br />
6.2.4 Fiberoptic Telemetry System Specific Configurations<br />
. . . .<br />
. . . .<br />
. . . .<br />
. . . .<br />
. . . .<br />
. . . .<br />
. . . .<br />
. . . .<br />
.6-5<br />
.6-6<br />
.6-6<br />
.6-7<br />
.6-7<br />
.6-9<br />
.6-9<br />
.6-9<br />
6.3 Fiberoptic Sensor Array Telemetry Transmission Line Parameters . . .6-11<br />
6.3.1 Transmission Line General Parameters . . . . . . . . . . . .6-11<br />
6.3.2 Transmission Line Specific Parameters . . . . . . . . . . . .6-11<br />
6.3.3 Multiplexing with Optical Fibers . . . . . . . . . . . . . .6-12<br />
6.3.4 Connector Parameters . . . . . . . . . . . . . . . . . . . .6-13<br />
6.4 End-Terminal (Receiver) Consideration . . . . . . . . . . . . . . .6-13<br />
6.5 Summary . . . . . . . . . . . . . . . . . . . . . . . . . . . . . .6-13<br />
APPENDIX - Fiberoptic Sensors Glossary. . . . . . . . . . . . . . . . . .A-l
CHAPTER 1<br />
INTRODUCTION<br />
1.1 BACKGROUND<br />
The ever-present need for increased communication<br />
aystem capacity and reduced cost per message<br />
unit has spurred the development and installation of<br />
hundreds of operating lightwave communication ayatems<br />
around the world. Compared to wire aystems, optical<br />
fiber transmission syatems operate with less energy per<br />
message unit-mile, lower signal attenuation per unit<br />
distance, higher bandwidth for increased channel capacity,<br />
lower electromagnetic interference, lower crosstalk,<br />
higher resistance to clandestine tapping, lower<br />
shock hazard, amaller size, less weight, reduced consumption<br />
of critical metals, and many others. These<br />
advantages have encouraged improvements in light<br />
sources; optical fibers, cables, and connectors; and<br />
photodetectors. Optical fiber data links are off-theshelf<br />
ready-to-install items. Hundreds of millions of<br />
dollars are being spent annually for improving optical<br />
communication system component.<br />
Capitalizing on the availability of optical<br />
components, there haa been significant progress during<br />
the past few years toward the development of a new<br />
claaa of sensors employing fiberoptic. These sensors<br />
are capable of detecting acoustic fields, linear and<br />
rotational acceleration, electric and magnetic fielda,<br />
and many other physical parameters. In effect, the<br />
senaor modulates some feature of the lightwave in an<br />
optical fiber such as the intenaity OT the phase.<br />
Usually phase modulation must be converted to an intensity<br />
modulation prior to detection. This may be accomplished<br />
by means of an optical interferometer. The resulting<br />
signals (intensity or phase) can be telemetered<br />
to places other than the location of the sensor (transducer,<br />
modulator) by means of a fiberoptic signal transmission<br />
(telemetry) system. The optical signal may be<br />
in analog or discrete form and the system may operate<br />
with or without optical-to-electrical or electrical-tooptical<br />
signal conversion. The fiberoptic aensors described<br />
in this manual may use fiberoptic transmission<br />
systems as well as electrical or electromagnetic transmission<br />
systems. Even for the simplest case, one in<br />
which a visual field or image is to be transmitted in<br />
a coherent-fiber cable, the fiber bundle itself must<br />
serve as the sensor and all the aspects of achieving<br />
lightwave acceptance by optical fibers must be considered.<br />
1.2 PURPOSE<br />
This manual on fiberoptic sensors is designed<br />
to be a stand-alone document intended to serve many purposes.<br />
It provides a basic background for understanding<br />
the concepts that make up the field of fiberoptic,<br />
particularly as they apply to fiberoptic sensors. It<br />
describea the propertied of optical fibers, then fabrication,<br />
and the properties of light sources and detectors<br />
associated with fiberoptic sensora. Specific<br />
emphasis is placed on design considerations for these<br />
major components and for associated connector,<br />
splices, couplers, and cables.<br />
Different schemes may be used for controlling<br />
lightwaves in order to sense a physical parameter. Many<br />
of these control schemes are discussed in this manual,<br />
including interferometry, polarization, and modulation.<br />
Intensity and phase modulation are discussed in terms<br />
of homodyne and heterodyne detection. Integrated optical<br />
circuits are introduced with emphasis on their fabrication<br />
and operating principles.<br />
Many different types of fiberoptic sensors<br />
are described in terms of their design and operation.<br />
Some of these include intensity and phase modulation<br />
sensora, rotation sensors, and accelerometers. Devices<br />
discussed include the fiberoptic sensora (transducers,<br />
modulators) used in hydrophores, magnetometera and geophones.<br />
In most fiberoptic sensor and sensor array<br />
applications there will be a requirement to telemeter<br />
sensed data over the full range of distances. Various<br />
fiberoptic aensor arrays and telemetry schemes are discussed.<br />
Information is given concerning risetime and<br />
power budgeting. Overall design considerations for telemetry<br />
systems are also briefly discussed.<br />
1.3 CONTENTS BY CHAPTER<br />
Following thia brief Introduction, (Chapter<br />
1), Chapter 2 is devoted to the properties of the baaic<br />
component of the fiberoptic sensor: the optical fiber<br />
itself. Electromagnetic wave (lightwave) propagation<br />
in optical fibera in terms of the wave equation; the<br />
coupling of lightwaves in and out of fibers; power loss<br />
by absorption, leakage, and scattering; are all discussed<br />
in some detail. Various properties of fibers, their<br />
basic construction and limitations are discussed, including<br />
basic concepts of total internal reflection,<br />
critical entrance angles, and numerical aperture. The<br />
concepts of mode propagation, refractive index profiles,<br />
and polarization are introduced. Various methods of<br />
fiber fabrication are covered, including several methods<br />
of drawing fibers. Obtaining deaired refractive<br />
indices and the size, strength, and level of purity of<br />
fibers are also described. Finally, in Chapter 2, the<br />
characteristics of various types of light sources are<br />
discusaed in sufficient detail to understand their use<br />
in connection with fiberoptic sensors. The chapter<br />
closes with a discussion of the characteristics and<br />
limitations of photodetectors with apecial emphasis on<br />
their importance and use in connection with the output<br />
signal from a fiberoptic sensor.<br />
Chapter 3 follows with a diacuasion of the<br />
various means for connecting fiberoptic aenaor inputs<br />
to electrical or optical sources and outputs to photo-<br />
1-1
detectors or display devices. The sensor may be connected<br />
to optical fibers and cables by various types<br />
of connectors, splices, couplers, mixers, and cables,<br />
the connector and splice being used primarily to join<br />
fibers and cables, the couplers being used to connect<br />
one source to many fibers (divergence), the mixer being<br />
used to couple many fibers to one photodetector (convergence).<br />
The operation of fiberoptic sensors cannot be<br />
well understood without an understanding of the varioua<br />
actions and interactions that can take place by and<br />
among lightwaves. Many of these interactions are the<br />
basis for sensing physical parameters. The lightwave<br />
characteristics discussed in Chapter 4 include interferometrics,<br />
polarization, and intensity and phase modulation<br />
in relation to homodyne and heterodyne detection.<br />
Chapter 4 ends with lightwave control technique<br />
used in integrated optical circuits.<br />
Chapter 5 turns primary attention from general<br />
principles and techniques used in the operation of<br />
fiberoptic aensora to a description of the sensors<br />
themselves and their components. Intensity modulation<br />
sensors; phase modulation devices, such aa those used<br />
in hydrophores and magnetometera; rotation sensors, accelerometers,<br />
and geophones are discuased as examplea<br />
of fiberoptic sensor applications.<br />
The grouping of fiberoptic aensors into senaor<br />
arrays and the telemetering of their outputs to<br />
other locations are covered in Chapter 6. Design options;<br />
basic configuration; riaetime, power, and coat<br />
budgeta; and specific configurations of fiberoptic<br />
arrays and telemetry aystema are diacuased in depth,<br />
along with light sourcea, transmission lines and endterminals<br />
as they relate to fiberoptic senaors.<br />
Bibliographies pertinent to the subject are<br />
included at the end of each chapter. The appendix contains<br />
an authoritative glossary of terms and definitiona<br />
in the field of fiberoptic with emphasia on the terms<br />
used to describe the design, fabrication, and operation<br />
of fiberoptic aenaors. Particular attention in the<br />
gloasary is devoted to the terms used in this manual.<br />
Many topics and concepta related to fiberoptic senaors,<br />
their operating principles, and supporting theory are<br />
included in the glosaary ao aa not to overburden the<br />
reader with too many detaila while the main topics are<br />
being discussed. For example, concepta concerning diaperaion,<br />
Msxwell’a equations , modulation, polarization,<br />
reflection and transmission coefficient, and various<br />
tvpes of fiberoptic sensors and interferometers are<br />
described in the glosaary.<br />
1-2
CHAPTER 2<br />
<strong>FIBEROPTIC</strong> <strong>SENSOR</strong> COMPONENTS<br />
2.1 OPTICAL FIBER PROPERTIES<br />
In this section the basic properties of optical<br />
fibers are discussed in some detail with emphasis<br />
placed on concepts that are important in optical fiber<br />
sensor technology. The structure of optical fibers is<br />
quite simple, as shown in Fig. 2.1. Basically they<br />
consist of layered cylinders of glass or plastic with<br />
small diameters. There is a central cylinder called<br />
the core, which is made up of one type of glass or<br />
plastic. Surrounding the core is a cylindrical shell<br />
called the cladding that is made of a slightly different<br />
type of glass or plastic. The difference between<br />
the core and cladding materials will be discussed later.<br />
Finally, this layered cylinder is usually surrounded by<br />
a Protective jacket. The light-guiding capability of<br />
the fiber is dependent upon the properties of the core<br />
and cladding while the mechanical strength of the fiber<br />
is maintained by the jacket that is usually made of<br />
plastic.<br />
CL’<br />
‘A’!” A<br />
INPUT<br />
Fig. 2.2<br />
MODULATING SIGNAL<br />
LIGHT PULSES<br />
OPTICAL<br />
DET&CT- .<br />
A basic optical fiber link.<br />
OUTPUT<br />
Four major optical fiber design objectives<br />
will be discussed. The first major objective is the<br />
desirability of maximizing the amount of available light<br />
that is transferred (coupled) into the core of the<br />
fiber. It is only the light in the core that is propagated<br />
along the length of the fiber with relatively low<br />
optical power loss. In order to maximize the amount of<br />
light transferred (coupled) into the core, it is necessary<br />
to maximize the numerical aperture (NA) of the<br />
fiber. This is one of four important fiber parameters<br />
that strongly affect the behavior of the simple system<br />
shown in Fig. 2.2. After introducing the other three<br />
important parameters, each will be discussed in some<br />
detail.<br />
The second fiber design objective is the de-<br />
1/ L sizability of minimizing the light lost from a beam as<br />
it travels through the core from the input end to the<br />
output end of the fiber. This light loss is described<br />
as the attenuation (power leas) rate, usually expressed<br />
in dB (decibel) per kilometer of fiber.<br />
CORE<br />
Fig. 2.1 The basic structure of an optical fiber.<br />
2.1.1 Design Objectives<br />
Some of the design objectives considered in<br />
the development of a good optical fiber are illustrated<br />
by the simple system shown in Fig. 2.2. The system consists<br />
of a pulse-modulated optical source. The input<br />
signal at the left represents the intelligence (information)<br />
that is impressed on (modulates) the light beam<br />
that, after emerging from the source, is focused with<br />
a lens into one end of an optical fiber. The light<br />
travels through the fiber and emerges from the opposite<br />
end, where it is directed into an optical detector<br />
(photodetector), possibly focused again with a second<br />
lens.<br />
The third optical fiber design objective is<br />
the desirability of maximizing the information carrying<br />
capacity of the fiber. The input to the fiber may be<br />
a light beam of continuously-varying intensity or a<br />
group of well defined pulses of light as shown in Fig.<br />
2.2. As the light pulses propagate through the fiber,<br />
their amplitude will decrease due to attenuation. In<br />
addition, due to a number of other effects to be discussed,<br />
the individual pulses also may broaden (spread).<br />
If they become too broad they will overlap or coincide<br />
with one another in both time and space. If this OCcurs,<br />
the intelligence (information) originally impressed<br />
on the light beam would be lost. Pulse broadening<br />
that occurs in the fiber is called dispersion. This<br />
parameter places a limit on a fiber’s information carrying<br />
capacity (signaling rate).<br />
The fourth design objective is the desirability<br />
of maximizing the strength of fibers when they are<br />
Initially drawn and maintaining this strength when the<br />
fibers are formed into cables or are used in sensors<br />
and other applications.<br />
Before considering these and other fiber design<br />
objectives in some detail, the basic theory of<br />
light propagation in optical fibers will be discussed,<br />
beginning with light-ray propagation in layered media.<br />
2-1
1<br />
The light-ray concept is a convenient approximate approach<br />
that may be used to introduce other important<br />
concepts such as total internal reflection and ray trapping.<br />
To extend the theory of light propagation farther,<br />
however, it is necesaary to take into account the<br />
notions that light is an electromagnetic wave phenomenon<br />
and that optical fibers are cylindrical dielectric<br />
waveguides. With these in mind it is possible to<br />
develop concepts regarding the allowed electromagnetic<br />
propagation modes of a cylindrical waveguide and to<br />
introduce the frequently encountered optical fiber waveguide<br />
V-Parameter (V-value) that must be considered<br />
when selecting a suitable fiber for a particular application.<br />
In accordance with the ray theory of light<br />
propagation, a light beam incident from below on the<br />
interface surface between two transparent media, at an<br />
angle e 1 with the interface surface behaves as shown in<br />
Fig. 2.3. When fll ia large, part of the incident beam<br />
Fig. 2.3<br />
MEDIUM2 ! .-”’”<br />
X6;<br />
n2<br />
k<br />
n1>n2<br />
Reflection and refraction at the interface<br />
when a lightwave travels from a higher to<br />
a lower refractive index medium.<br />
is transmitted into the upper medium and vart is reflected.<br />
Their relative intensities depend upon the<br />
refractive indices of the two media. The refractive<br />
index of a medium is defined as the ratio of the velocity<br />
of light in a vacuum to the velocity of light in<br />
the medium. The higher the refractive index of a medium<br />
the slower light will travel in it. The refractive<br />
index of medium 1 is designated as nl and that<br />
for medium 2 as n2 as shown in Fig. 2.3.<br />
These indices alao determine the direction<br />
of the beam transmitted into medium 2, i.e., @2 in<br />
Fig. 2.3 is determined by the indexes of both media.<br />
Snell’s law of refraction of light at an interface predicts<br />
that the ratio of the cosine of the angle 131 to<br />
the cosine of the angle of t12 is equal to the ratio<br />
n2/nl which is equal to the velocity ratio v1/v2. Thus,<br />
as shown in Fig. 2.3, if light propagates in medium 1<br />
at a lower velocity than in medium 2, the angle 01 will<br />
be greater than the angle 02 and the ray will be bent<br />
toward the interface when entering medium 2. The angle<br />
of the reflected beam is equal to the angle of the incident<br />
beam. These are an application of the well known<br />
laws (Snell’s laws) of refraction and reflection that<br />
aPPIY in ray treatments of wave phenomena.<br />
nl > n2<br />
+’*NG)<br />
v,< V2<br />
I \ MEOIUMI’(CORE)<br />
CASEI 01>0, CASE2 e)=ec CASE3: 01 n2. There is both a refracted and a reflected<br />
beam and, from the conservation of energy, the sum of<br />
their energies must equal the energy in the incident<br />
beam.<br />
2-2<br />
Fig. 2.5<br />
A step-index optical fiber showing the<br />
critical angle, 6C for total internal reflection.
fleeted each time it is incident on the core-cladding<br />
interface so that it remains ““trapped”” in the core.<br />
This, and any other ray with f31
”’’-” [--::=<br />
----<br />
\<br />
.! (<br />
ACCEPTANCE<br />
&<br />
CONE<br />
J-’’”<br />
Fig. 2.8<br />
The acceptance cone for a ~tep~i~~$x optical<br />
fiber. (N. A.=sinec=(nl ‘n2 )<br />
end surface, where the refractive index of air, no7 IS<br />
equal to unity, there is another critical angle,3c ,<br />
such that all ,the light contained within the cone of<br />
half angle Clc , will be trapped within the fiber. Applying<br />
Snell’s Law, this time in the sine form because<br />
ec ‘ is the angle between the cone edge (elements) and<br />
the normal to the surface of incidence (end face of fiber),<br />
the ratip of the sine of ec within the core to<br />
the sine of ec in air is equal to the refractive index<br />
n. of air divided by the refractive index nl of the<br />
core. Thus, since n. = 1:<br />
(sinoc)/no = sinec = (sin9c’)/nl (2.8)<br />
At the core-cladding interface within the fiber it was<br />
shown that Cosoc = n2/nl Eq. (2.3). Combining Eqs.<br />
(2.3) and (2.8) and using the Pythagorean theorem:<br />
sin28c + c0s20c=l=(sin20c’ )/n12 + n22/n12 (2.9)<br />
Transposing:<br />
(5in2ec’ )/n12=l-n22/n12=(n12-n22)n12 (2.10)<br />
Thus, from the defini~ion that the numerical aperture<br />
is equal to the sin ec” :<br />
As<br />
2 1/2<br />
N.A. = sinoc’ = (n12 - n2 ) (2.11)<br />
defined in Eq. (2.2) above:<br />
Solving for n2:<br />
A = (nl - n2)/nl (2.12)<br />
n2 =<br />
nl (1 - A) (2.13)<br />
Substituting Eq. (2.13) in Eq. (2.11) and simplifying:<br />
N.A. = nl(2A - A2)1/2 (2.14)<br />
If A2 !9’<br />
~<br />
A<br />
Light rays in a step-index fiber core.<br />
Two rays are ,showo in Fig. 2.9. One enters<br />
from air at an angle, 0 , such that on intersecting the<br />
core-cladding interface, it makes an angle less than<br />
the critical angle, 13c, with the interface. This ray<br />
will be totally internally reflected and will be trapped<br />
in the core, so that it propagates with minimal<br />
loss through the fiber core. A second ray, incident<br />
from air at a larger angle, intersects the core-cladding<br />
interface at an angle greater than tic. At each<br />
reflection part is reflected back into the core and<br />
part is transmitted into the cladding. Such a ray is<br />
strongly attenuated, rapidly decreasing in intensity<br />
as it propagates along the core of the fiber.<br />
The Eqs. (2.8), (2.11) and (2.15) show that<br />
the critical angle at the core-cladding interface for<br />
total internal reflection in radian measure for the<br />
trappin of light in the core is approximately equal<br />
to (ti) f 12 when A2
6=0<br />
REFERENCE PLANE<br />
that propagate along the axis of the guide each with a<br />
discrete velocity.<br />
,> = (J<br />
REFERENCE LI<br />
z<br />
In order to characterize light propagation in<br />
a step-index optical fiber it is convenient to use a<br />
parameter, usually referred to as the waveguide V-parameter<br />
(V-value). It is defined by the equation:<br />
V = 2ma(nl<br />
and therefore from Eq. (2.11):<br />
2- 2 112/i<br />
n2 ) o (2.18)<br />
V = 2~a(N.A.)/& (2.19)<br />
Fig. 2.10 The cylindrical coordinate system for expressing<br />
lightwave propagation in an optical<br />
fiber. The point P is designated as p,<br />
0, z.<br />
The Z-axis of this coordinate system is taken<br />
to be the central axis of symmetry of the waveguide.<br />
The z-coordinate is the distance from a reference plane<br />
designated as Z. (zEO). A spatial point in a fiber is<br />
located by defining a radius coordinate, p, as the distance<br />
radially from the Z-axis; an azimuthal (angular)<br />
coordinate, $, measured from an arbitrary reference<br />
plane ($=0); and a value of z. This coordinate system<br />
is commonly known as the cylindrical coordinate system.<br />
In the simple case where the refractive index<br />
depends only on the radial coordinate, the solution to<br />
the wave equation, derived from Maxwell’s equations for<br />
the electric fields, can be expressed as the product<br />
of two functions as follows:<br />
where a is the core radius; N.A. is the fiber numerical<br />
aperture, a function of the refractive indices of the<br />
core and cladding; and i. is the wavelength of the incident<br />
light in a vacuum. (The wavelength of a lightwave<br />
in a vacuum is nearly equal to its wavelength in<br />
air.) These are the main parameters needed to describe<br />
light propagation in a step-index optical fiber. The<br />
V-parameter may be designated as the light propagation<br />
characteristic of an optical fiber. The larger the V-<br />
value the larger the number of modes (different discrete<br />
waves) the fiber can support, i.e., allow to propagate.<br />
The predictions or conclusions that may be<br />
drawn from the wave theory of light propagation in<br />
fibers may be summarized in graphical form. As already<br />
mentioned, only particular (discrete) solutions of the<br />
wave equation exist. These correspond to discrete waves<br />
propagating along the axis of the guide with particular<br />
velocities. Some of the characteristics of these particular<br />
(allowed) modes are shown in Fig. 2.11. The<br />
kn,<br />
E(p, $,z,t) = E(p, $)e-j(~t-W) (2.16)<br />
= E(p, $)sin(ut-&) (2.17)<br />
The variable t is the time measured from a time reference<br />
of to. The first is an amplitude factor E(P ,$)<br />
that depends on the radius vector P and the azimuthal<br />
(angular) coordinate $. The second, which can be expressed<br />
as complex exponential or sinusoidal function,<br />
indicates that the electric fields are sinusoidal waves<br />
in time and in space. The angular frequency is u= 2nf<br />
where f is the optical frequency. The B is the propagation<br />
constant, defined as the refractive index, n,<br />
times the z component of the wave vector k, where kn=<br />
2h/io, and i. is the optical wavelength in a vacuum at<br />
frequency f. Thus, optical energy transfer in dielectric<br />
media takes place in the form of wave propagation<br />
along the axis of the guide. The absolute value of k<br />
is also called the wave number.<br />
2.1.3 Propagation Modes<br />
When the geometric boundary conditions at the<br />
core-cladding interface are introduced only particular<br />
(discrete) solutions of the wave equations are permitted.<br />
Only these values can exist, each designated by a<br />
value for i, for the amplitude factor Ei(P,$) and cor -<br />
responding discrete values for the propagation constant<br />
~. The velocity of propagation of each allowed wave,<br />
i.e. mode, along the axis of the waveguide is given<br />
by the ratio of the angular frequency divided by the<br />
propagation constant Bi, of a particular wave designated<br />
by the subscript. Thus, the various allowed solutions<br />
represent discrete waves with discrete amplitudes<br />
2-5<br />
kn2<br />
V=? G<br />
wAVEGUIDE PARAMETER<br />
Fig. 2.11 The propagation constant, i3, and the velocity<br />
of various modes as a function of the<br />
V-parameter of an optical fiber.<br />
curves show the allowed values of the propagation constant<br />
& as a function of the V-parameter (V-value).<br />
Each curve corresponds to a particular allowed solution<br />
of the wave equation. This graph indicates that the<br />
allowed values of %for the various solutions are in<br />
between knl and kn2, corresponding to the wave numbers<br />
in the core and in the cladding, respectively. Since<br />
the wave (phase) velocity in the Z-direction is given<br />
by the quantity m/6 the curves in Fig. 2.11 also show<br />
the phase velocity versus the waveguide V-parameter (Vvalue).<br />
Thus, the velocity of the allowed waves (modes)<br />
represented by the different curves is seen to range<br />
from the higher velocity in the cladding (lower ordinate,<br />
higher value) to the lower velocity in the core<br />
(upper ordinate, lower value) as the waveguide V-parameter<br />
increases. Thus each curve in Fig. 2.11 corresponds<br />
to an allowed solution of the wave equation applied<br />
to dielectric waveguides. The waveguide V-para-
1<br />
meter varies directly with the core radius and numerical<br />
aperture and inversely with the wavelength of light.<br />
As the V-parameter increases, the number of allowed<br />
modea increasea. For V less than 2.40, only one wave<br />
or mode, designated in Fig. 2.12 as the HE1l mode,<br />
ia permitted. For V in the range of 2.4 to 3.8, four<br />
modes are allowed, these being the HE1l, TEOl, TMol,<br />
and HE21 modes. These particular alphanumeric designations<br />
are standard for electromagnetic waveguides.<br />
They have been chosen because of the specific forms<br />
of the spatial variations for the electric and magnetic<br />
fields associated with the particular solutions for the<br />
wave equation. As V increases, more and more modes are<br />
permitted (supported).<br />
Consider the specific case in which V is less<br />
than 2.40 as shown in Fig. 2.12. This is especially<br />
k“,<br />
pattern is circularly symmetric and shows no fine structure.<br />
Horizontally polarized light could also have<br />
been introduced into the same fiber at the same time.<br />
Such light would remain horizontally polarized in an<br />
ideal fiber. In fact this same type of behavior applies<br />
to any direction of polarization and gives rise<br />
to one scheme for multiplexing.<br />
In an ideal singlemode fiber with perfect cylindrical<br />
symmetry the direction of light polarization<br />
once introduced remains constant and there is no energy<br />
transfer among the waves with different polarization<br />
directions. However, in real fibers, due to slight<br />
ellipticities in the core cross section, imperfections<br />
in the core cladding interface, variations in the refractive<br />
indices throughout the core, effects due to<br />
bending, and other causes, there is usually some coupling<br />
between the different directions of polarization<br />
and some variations in the velocity of each of the<br />
waves with different polarizations. These effects must<br />
be considered in certain applications. They will be<br />
diacussed later when lightwave polarization effects in<br />
ainglemode fiberoptic sensor applications are considered.<br />
Returning again to a consideration of the spatial<br />
modes of lightwaves in optical fibers, consider<br />
the case of a fiber that can support four separate electromagnetic<br />
modes. This occurs when the V-value is in<br />
the range 2.4 < V < 3.8, as shown in Fig. 2.13. The<br />
WAVEGUIDE PAR&METER<br />
V<br />
1 ,..<br />
//EEE1 *:. :;:( ~Eol<br />
HE)) I .<br />
!+.3,<br />
T,o,<br />
“,22<br />
& @<br />
CLADDING<br />
.--——- ,~,,<br />
HE,,<br />
,.21
in the right center of Fig. 2.13. They increase in<br />
magnitude from zero along the axis of the core to a<br />
maximum and then decay as the core-cladding interface<br />
is approached, as shown in the lower right. As already<br />
pointed out for the HE1l mode in this case, the fields<br />
again extend beyond the core into the cladding.<br />
Returning to the graph at the left in Fig.<br />
2.13, as V is increased further, for example by decreasing<br />
the wavelength, ,10, of the light injected into<br />
the fiber, additional relatively lossless modes are permitted<br />
and, very rapidly, propagation phenomena change<br />
from the single or few mode types to multimode behavior.<br />
In fact, for V > 10 the number of allowed modes is approximately<br />
equal to V2/2 for a step-index fiber. As<br />
already pointed out above in the discussion of the radial<br />
electric field distribution for the HE1l and TEOl<br />
modes, shown in the lower right in Fig. 2.12 and 2.13,<br />
respectively, the ~-fields may extend well beyond the<br />
core cladding interface. In fact when each mode is<br />
first allowed much of its energy is associated with<br />
fields that penetrate the cladding. This phenomena is<br />
shown in Fig. 2.14 where the ratios of the power in the<br />
cladding, pclad, to the total power, F’, in a particular<br />
mode are plotted as functions of the V-parameter. At<br />
low values of V, for example V less than 1.0, most of<br />
the energy transmitted by the HE1l mode is associated<br />
with the field in the cladding. The spatial character<br />
of each new allowed mode becomes more complex within<br />
the V-values, for example, most of the energy transmitted<br />
by the HE1l mode is associated with the fiel~s in<br />
$he cladding. As the V-value is increased, the E and<br />
H fields of the HE1l mode extend a smaller distance<br />
into the cladding and a larger portion of its transmitted<br />
energy is confined to the core, reading approximately<br />
80% of the total when V = 2.4, as shown in Fig.<br />
2.14. At this value of V, the TEOl, TMOl, and HE21<br />
modes first come into existence and initially, again,<br />
pcladtpz 1. As the V-value increases further the energy<br />
associated with these three modes also become more confined<br />
to the core. At V = 3.8, three additional modes,<br />
the HE12, EH1l, and H31, are allowed. In this case, due<br />
to the radial and azimuthal structure of their ~ and P<br />
fields they initially propagate with approximately half<br />
of their energy in the core and half in the cladding,<br />
so that the power ratio Pclad/P starts off at 0.5 and<br />
and then decreases rapidly as V increases.<br />
This characteristic of mode propagation in<br />
optical fibers is employed to advantage in a number of<br />
fiber sensor applications. It is the basis of operation<br />
of evanescent wave couplers, or beam splitters,<br />
wherein a portion of the light propagating in one fiber<br />
is transferred to a second fiber by bringing their<br />
cores close together by etching or lapping away a portion<br />
of the cladding. Another application of this same<br />
phenomenon is as the transduction mechanism in a number<br />
of different intenaity-type aensors, where, through<br />
carefully controlled micro-displacements induced by<br />
bending, light can be ejected from the loosely-bound<br />
high-order core modes. These and other useful applications<br />
of this core-into-cladding energy transfer of the<br />
electromagnetic wave fields are discussed in detail in<br />
later sections.<br />
After the above brief discussion of the ray<br />
and the waveguide theories of light propagation in optical<br />
fibers, it is appropriate to return to a more<br />
general consideration of the macroscopic propertied of<br />
fibers. The conceut of attenuation will be discussed<br />
next. Assume that-a pulse of light, of peak intensity<br />
(optical power) 1., is injected at the left into the<br />
core of a fiber, as shown in Fig. 2.15. In general, as<br />
OUTPUT INTENSITY DECREASES WI’H INCREASING<br />
IIZ)=Ioe–az<br />
Fig. 2.14 The variation of the ratio of optical power<br />
in the cladding to the total optical power<br />
in a fiber as a function of the V-parameter<br />
(V-value).<br />
ATTENUATION EXPRESSED IN DECIBELS PER KILOMETER (dB/km)<br />
I(z)<br />
FOR Z . 1 km, dB/km=–lOloglo~<br />
2-7<br />
Fig. 2.15 Light intensity (optical power) relative<br />
attenuation as a function of distance in an<br />
optical fiber.<br />
it propagates through the fiber its intensity, I, will<br />
decrease exponentially so that the intensity of any<br />
point (transverse plane) z in the fiber is given by:<br />
I(z) = Ioe-az (2.20)<br />
where 10 is the intial intensity of the point of entry<br />
into the core (z = O), z is the longitudinal distance<br />
along the fiber, and = is the intensity attenuation coefficient.<br />
Thus, as indicated in the graph in Fig.<br />
2.15, if in traveling a particular distance, z1, the<br />
intensity decreases to 0.51., then at z = 2z1, it will<br />
be 0.251., i.e., at the end of each Z1 incremental in-
crease in distsnce the intensity is reduced to l/2 of<br />
the intensity at the beginning of the incremental increase.<br />
For example, for this case, at the end of 521<br />
the intensity will be 2-5 = 1/32 of the initial value.<br />
For optical fibera, the attenuation rate is uaually<br />
specified in terms of the decibels loss per kilometer,<br />
i.e., (dB/km). In the case of z = 1 km, the attenuation<br />
rate may be defined by the equation:<br />
Attenuation Rate = -10 loglO(I1/Io) dB/km (2.21)<br />
In a fiber with an attenuation rate of 10 dB/km the intensity<br />
(optical power) will fall to one tenth of the<br />
incident intensity after traveling one kilometer. A 3<br />
dB/km attenuation rate corresponds to a reduction to<br />
one half the incident intensity after one kilometer,<br />
since loglo 0.5 is equal to 0.3. In this latter caae,<br />
after 5 km the intensity would be down 15 dB from the<br />
initial value, i.e., the attenuation will be 15 dB.<br />
A historical picture of the change in attenuation<br />
rates of available fibers, from about 1968 to the<br />
present, is shown in Fig. 2.16. The graph indicates<br />
o<br />
0<br />
‘%a<br />
0011 I , , , , ,<br />
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absorption, ia due to absorption of optical energy into<br />
the electronic energy levels of transition metal impurities,<br />
such as iron, copper, chromium and nickel, and<br />
into the vibrational levela of hydroxyl ions (OH-) in<br />
the core and innermost sections of the cladding. In<br />
this case, energy is absorbed from the optical beam and<br />
reradiated into the molecular lattice in the form of<br />
heat. The second type of attenuation is due to bendin~<br />
losses of which there are two typea. One is due to<br />
:regular bending of the entire fiber at nominal radii.<br />
For example, bending loss may be due to winding the fiher<br />
on a small-diameter mandrel. The second, referred<br />
1:0 as mlcrobend loss, arise because of random variations<br />
in the direction of the axia of the core. These may<br />
even be microscopic, due to external forcea, imperfections<br />
in the coating or cladding, ripples in the core-<br />
(:ladding interface, ticrocracks, and other causes. In<br />
either caae, light will be injected from the core into<br />
the cladding, and thus cause a decreaae in the light<br />
intensity transmitted through the core to the output<br />
end of the fiber. Finally, there are three types of<br />
scattering losaes. The first, called Rayleigh scattering<br />
la cauaed by microscopic density fluctuation that<br />
are frozen into the random molecular structure of the<br />
glass making up the fiber core when it cools to its<br />
relatively high solidification temperature. These density<br />
fluctuations may be resolved into spatial frequencies<br />
that have wavelengths much shorter than the optical<br />
wavelength. Rayleigh scattering losses vary inversly<br />
as the fourth power of the optical wavelength. In addition<br />
to the static denaity fluctuations, there are also<br />
dynamic density fluctuation due to thermal sound waves.<br />
These waves originate and propagate becauae the temperature<br />
of the glass is above absolute zero. These propagating<br />
density fluctuations (thermal phonons) lead to<br />
Brillouin scattering. Finally, there is scattered<br />
light caused by absorption and reradiation from atomic<br />
vibrational and rotational energy levels, i.e., Raman<br />
scattering. These latter two scattering processes,<br />
i.e., Brillouin and Raman, are non-linear processes<br />
and are significant only at high optical intensities.<br />
The strength and wavelength-dependence of<br />
some of these loss mechanisms is shown in Fig. 2.17.<br />
Fig. 2.16<br />
The reduction of fiberoptic attenuation<br />
rates over the years. The + is a projected<br />
value.<br />
351<br />
I I I I I I<br />
why fiberoptic communication links were impractical in<br />
the late 1960’a, since attenuation rates in the range<br />
1000 to 100 dB/km correspond to a decrease to one tenth<br />
of the input intensity after traveling only 10 to 100<br />
metera, respectively. A very evident atep decreaae in<br />
attenuation rate occurred around 1970, with the introduction<br />
of a new fiber fabrication technique, the vapor<br />
phaae deposition proceas. This led to the availability<br />
of the first high-priority silica fibers, and the development<br />
of a group of related techniques for producing<br />
extremely high purity, low leas fibers. Today fibers<br />
are available with minimum lossea, at selected<br />
wavelengtha, in the range 0.2 to 1.0 dB/km so that the<br />
repeaterless optical communication links of longer than<br />
50 kilometer are an achievable reality.<br />
A clear understanding of the factors that effect<br />
attenuation in optical fibers is of importance not<br />
only to the fiber designer but also to the fiber user.<br />
The causea of attenuation may be divided into<br />
three aeparate categories: The first, called material<br />
2-8<br />
30<br />
25<br />
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20<br />
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15<br />
x<br />
0 J<br />
10<br />
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05 06 07 08 09 10 11<br />
WAVELENGTH (MICRONS)<br />
● TRANSITION METAL IMPURITIES (Fe, Cu, Cr,Ni)<br />
● HYDROXLION (OH)-1 PPM—~ldB/km@.95#m<br />
● RAYLEIGH SCATTERING w l/A4<br />
● LEAKAGE LOSSES (MICROBEND, REGULAR BEND, ETC.)<br />
Fig. 2.17 Sources (causes) of optical power attenuation<br />
rate as a function of wavelength in a<br />
typical optical fiber.
The vertical height of the various cross-hatched regions<br />
represent the loss as a function nf the wavelength<br />
arising from the various sources. Note that the<br />
minimum total attenuation at approximately 0.8 micron<br />
wavelength is approximately 10 dB/km. This is a somewhat<br />
mediocre fiber by today’s standards. The lowest<br />
four regions in Fig. 2.17 correspond to the loss due<br />
to 1 part per million by weight, in silicon oxide (Si02)<br />
glass, of the metallic impurities Cu, Ni, Fe, and Cr,<br />
from bottom to top, respectively. The peak in the<br />
vicinity of the 0.95-micron wavelength is due to the<br />
third harmonic of the hydroxyl (OH-) vibrational mode,<br />
and corresponds to roughly a 20-part-per-million impurity<br />
content. The black dots are predicted values of<br />
losses based on calorimetry-type optical absorption<br />
measurements made on the glass sample from which the<br />
fiber was drawn. The upper cross-hatched region represents<br />
the attenuation due to Rayleigh scattering while<br />
the white region is the remaining difference between<br />
the total loss versus wavelength (the uppermost curve)<br />
and the sum of the previously mentioned losses. The<br />
latter is attributed to regular bending and microbending<br />
losses.<br />
The attenuation versus wavelength curve shown<br />
in Fig. 2.18 is for a currently available very-low-<br />
5.0 . ‘.<br />
3.0 — ‘.> ‘.<br />
2.0 —<br />
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1.0<br />
tion. In the bent region, the ray intersects the corecladding<br />
interface at an angle 13 that is greater than<br />
‘dC and thus it will be partially transmitted out of the<br />
core and into the cladding. This will occur at each<br />
successive reflection from the outer interface and large<br />
losses may occur. Another qualitative explanation of<br />
this type of loss is as follows. In the beam propagating<br />
in the fiber, assuming plane wavefronts, if the<br />
velocity at the center of the core in the bent section<br />
were equal to the c/nl, the “proper” velocity in the<br />
core, then the velocity at the outer edge of the front<br />
would have to be higher than c/nl, which cannot occur.<br />
Radiation in the form of core-to-cladding scattering<br />
results. Finally, from the electromagnetic wave theory<br />
it may be shown that in a waveguide with a constant<br />
bend radius, all of the solutions of the wave equation<br />
represent waves that decay with<br />
along the centerline of the core.<br />
increasing distance<br />
6<br />
6< 9.<br />
e’ 70,<br />
\<br />
/<br />
/<br />
/<br />
0.5 -<br />
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Fig. 2.19 Leakage of optical power froman optical<br />
fiber at a constant-radius bend.<br />
Fig. 2.18<br />
0.6 0.7 0.8 0.9 1.0 1.1 1.2 1.3 1.4 1.5 1.6<br />
WAVELENGTH (pm)’<br />
Attenuation rate of optical power in a low-<br />
10SS optical fiber as a function of wavelength.<br />
The arrows along the abscissa indicate<br />
the wavelengths of commercially<br />
available lasers.<br />
loss, single mode fiber. The arrows along the lower<br />
abscissa correspond to the wavelengths of currently<br />
available lasers. The peak in the loss curve at the<br />
1.4-micron wavelength is due to the OH- radical, which<br />
has been reduced to a relatively low concentration<br />
level. The minimum at approximately the 1.3 micron<br />
wavelength is of special interest, not only because the<br />
attenuation rate is down to 0.5 dB/km, but also because<br />
this wavelength is very close to the zero-dispersion<br />
wavelength of Si02 which is of special interest in some<br />
applications, as will be discussed shortly. Fig. 2.18<br />
shows that extremely low attenuation rates attainable<br />
with current fiber fabrication techniques at wave -<br />
lengths where high intensity long-life, solid state<br />
laser sources are becoming commercially available. It<br />
is now up to the fiber user to devise techniques and<br />
configurations that can maintain this low loss by not<br />
introducing significant regular (macro) bending and<br />
microbending losses.<br />
Using the latter approach it is possible to<br />
compute the expected loss due to a constant bend radius.<br />
The results of such calculations are shown in Fig. 2.20,<br />
where loss curves versus bend radius are shown for<br />
singlemode fibers at the 0.83-micron wavelength having<br />
different numerical aperture (N.A.). Note the strong<br />
dependence on bend radius and N.A. Referring to Fig.<br />
2.20, consider a fiber with a numerical aperture of<br />
0.1. When a 10-meter length is wound on a l.2-cmradius<br />
mandrel, the attenuation due to bending is approximately<br />
6 dB, i.e., 75 percent of the light energy<br />
injected into the core at the input end is scattered<br />
out of the core while propagating in the ten meters<br />
to the output end. Nhen 10 meters of identical fiber<br />
are wound on a 1.0 cm radius mandrel, the attenuation<br />
due to bending will increase by a factor of about<br />
250,000 to 60 dB, so that only about one millionth of<br />
the original light remains at the end of the fiber.<br />
Just about all of the input light is scattered out of<br />
the core. On the other hand, using the 1.2 cm radius<br />
mandrel and increasing the numerical aperture (N.A.)<br />
to 0.12 reduces these attenuations to 0.16 dB and 1.6<br />
dB, respectively. Therefore, care must be taken in<br />
designing fiberoptic sensors that require bending and<br />
winding of fibers and in specifying fibers for such<br />
applications.<br />
A ray picture of the regular (constant) bend<br />
radius loss mechanfsm is shown in Fig. 2.19. Assume a<br />
ray is traveling to the right at an angle of o less<br />
than the critical angle ec in the straight fiber sec - 2-9
-2 3 4 5 6 7 8 9 10 11 12<br />
BEND RADIUS (mm)<br />
Fig. 2.20 The variation of optical power attenuation<br />
rate as a function of bend radius for constant<br />
radius bends in typical optical fibers<br />
for various values of constant numerical<br />
apertures (N.A.) using 0.83-micron wavelength<br />
light.<br />
C.H. Bulmer, private communication.<br />
Fig. 2.21<br />
The effect of a microbend on ray propagation<br />
in an optical fiber is shown in Fig. 2.21. A ray pro-<br />
+==2si-<br />
The angle between an incident ray and the<br />
core-cladding interface surface exceeds the<br />
critical angle and therefore total internal<br />
reflection does not occur at the microbend,<br />
allowing part of the ray to leave the core<br />
and enter the cladding.<br />
pagating in the core at less than the critical angle<br />
is totally reflected before it reaches a section of<br />
fiber distorted by a small imperfection. On successive<br />
reflections from the core-cladding interface it is incident<br />
at an angle with the interface surface larger<br />
than the critical angle so that some light is transmitted<br />
into the cladding. Random distortions such as this,<br />
due to imperfections in the core-cladding interface or<br />
due to bending or tensile forces exerted at scattered<br />
points along the interface surface of the fiber can induce<br />
microbends in the core surface that lead to substantial<br />
cumulative losses. Such distortion losses are<br />
usually undesirable and detrimental, for example, when<br />
they arise in fiber cabling operations. on the other<br />
hand, microbending is employed in fiberoptic sensors<br />
as a transduction mechanism, as will be discussed later.<br />
2-1o<br />
The optical fiber property to be considered<br />
last is velocity dispersion, i.e. , differences in velocity<br />
among various portions of the light that may be<br />
propagated in the core of a particular fiber. It will<br />
be shown later how dispersion directly affects the behavior<br />
of specific fiberoptic sensors. For now, the<br />
significance of dispersion will be illustrated in terms<br />
of how it affects pulse broadening and thus limits<br />
bandwidth in fiberoptic data links and other communication<br />
applications.<br />
In the introduction to this chapter, it was<br />
pointed out that one of the aims of the optical-fiber<br />
designer is to design a fiber that will preserve the<br />
information impressed on a beam of light as it propagates<br />
through its core. A measure of success in this<br />
regard, as pointed out in the discussion of Fig. 2.2,<br />
Subsection 2.1.1, is how well the width of an individual<br />
narrow pulse is maintained without broadening.<br />
When a light pulse is injected into a step-index multimode<br />
fiber, its energy is divided among several different<br />
modes. Each mode travels at a particular velocity,<br />
or range of velocities, and thua they may arrive at the<br />
output end of the fiber at different times depending on<br />
their velocity and the length of the path they take.<br />
Obviously this contributes to pulse broadening and, in<br />
fact, this modal dispersion is the major source of pulse<br />
broadening in step-index multimode fibers. This type<br />
of dispersion is reduced substantially in graded-index<br />
multimode fibers in which the various modal propagation<br />
times are nearly equal to one another and thus<br />
the various portions of an injected pulse arrive at the<br />
end of the fiber at the same time though their propagation<br />
velocities and paths will differ. In this case,<br />
however, the next lower level of pulse broadening effects<br />
becomes evident. This is the so-called material<br />
or chromatic dispersion that occurs because the velocity<br />
of an electromagnetic (light) wave is usually a<br />
function of the wavelength in dielectric material. If<br />
an optical source emits a pulse of other than purely<br />
monochromatic (single-wavelength) radiation, the various<br />
wavelengths preaent will propagate at different<br />
velocities and thus lead to pulse broadening.<br />
The effects of modal and material dispersion<br />
are shown in Fig. 2.22 where the theoretically-predicted<br />
dipersion or pulse broadening, expressed in nanoseconds<br />
increase of pulse width for each kilometer of<br />
travel in a fiber, is plotted as a function of numerical<br />
aperture (N.A.) for various operating conditions.<br />
Two types of 0.85 micron nominal wavelength optical<br />
sources are considered. One is an injection laser emitting<br />
light with a apectral width (linewidth or variation<br />
of wavelength) of 20 Angstroms. The other is a<br />
light emitting diode (LED) emitting light with a spectral<br />
width (linewidth) of 350 Angstroms. When narrow<br />
pulses of light are injected into either graded-index<br />
or step-index fibers, Fig. 2.22 shows that for laser<br />
sources and for numerical apertures less than 0.15, the<br />
predicted broadening is only 0.2 nsec/km for the graded-index<br />
fiber, however, the dispersion is more than 10<br />
nsecfkm for the step-index fiber. This increase is due<br />
to modal diaperaion, because increasing N.A. corresponds<br />
to increasing the waveguide V-parameter so that<br />
additional optical modes are allowed. Initially at low<br />
N.A. values with the light emitting diode, material dispersion<br />
leads to a broadening of approximately 5 nsec<br />
per km in commercially available step-index and graded-index<br />
fibers,<br />
further increases<br />
values.<br />
and then modal dispersion leads to<br />
in step-index fibers at higher N.A.
60<br />
40<br />
20<br />
10.C<br />
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00.8<br />
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AO = 0.85 pm<br />
LED S1 FIBER<br />
/<br />
PRACTICAL LED<br />
PRACTICAL LASER<br />
GI FIBER<br />
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shown in Fig. 2.18. There are two other types of dispersion<br />
effects that usually occur when singlemode fibers<br />
are employed. The first of these is called waveguide<br />
dispersion which results from the variation in<br />
the propagation constant, B, or wave velocity (phase<br />
velocity), clneff, with changes in the V-parameters,<br />
and thus the wavelength, 1. This was considered earlier<br />
in the discussion of Fig. 2.11, but for the present<br />
discussion, it is useful to present the same information<br />
in another form as follows.<br />
In Fig. 2.23, typical curves of the optical<br />
angular frequency, w, are plotted as functions of the<br />
propagation constant, 6, for a few of the lower-order<br />
allowed modes in a fiber waveguide. This graph shows<br />
RADIATION<br />
MODE<br />
REGION<br />
cln~<br />
0.1<br />
I 1 I I I I I I I II I I I I 1 I I I I I I I I I I I<br />
o 0.05 0.10 0.15 0.20 0.25 0.28<br />
NUMERICAL APERTURE<br />
Fig. 2.22 The variation of dispersion in nanoseconds<br />
per kilometer as a function of numerical<br />
aperture (N. A. ) for step-index (S1) and<br />
graded-index (GI) optical fibers driven by<br />
laser or LED optical sources.<br />
After C. Keo and J. Goell,<br />
16, 1976.<br />
Electronics, 113, Sept.<br />
The above results also can be expressed in<br />
terms of the bandwidth of the modulation signals that<br />
may be transmitted by fibers. The bandwidth capacities<br />
(bandwidth-length product) currently attainable with<br />
various types of available fibers are summarized as<br />
follows:<br />
Modal-dispersion-limited behavior:<br />
Step-index fibers:<br />
Graded-index fibers<br />
Research grade<br />
Production grade<br />
Material-dispersion-limited behavior:<br />
Graded-index fibers (0.85 Urn):<br />
LED (350 ~ spectral ~idth)<br />
Injection laser (20 A)<br />
30 MHz-km<br />
1000 MHz-km<br />
400 MHz-km<br />
150 MHz-km<br />
2500 MHz-km<br />
The capacities are expressed as the product<br />
of the highest modulating frequency in megahertz that<br />
can be applied (without excess decay) multiplied by the<br />
fiber length in kilometers. Thua, using high quality<br />
graded-index multimode fibers, it is now possible to<br />
send signals with frequency components in excesa of 1<br />
GHz over fiber lengths approaching 1 km, or in excess<br />
of 5 GHz over fiber lengths approximately 200 m, and<br />
so on.<br />
In singlemode fibera, material or chromatic<br />
dispersion IS a significant factor. In silicon oxide<br />
(si02), the main constituent of the core and cladding<br />
of most high-grade glass fibers, the curve of the refractive<br />
index as a function of the optical wavelength<br />
has a minimum point at approximately 1.3 microns as<br />
2-11<br />
Fig. 2.23<br />
----<br />
~ ‘MODE ~<br />
PROPAGATION CONSTANT B<br />
The optical angular frequency, u, as a<br />
tion of the propagation constant, B, for a<br />
few low-order modes for lightwaves propagating<br />
in typical optical fiber, showing<br />
the phase and group velocities.<br />
the difference between the phase velocity of a singlefrequency<br />
continuous optical beam and the group velocity<br />
of an optical pulse. The wave velocity (phase<br />
velocity) is defined by the values of the ratio u/fi for<br />
any point on the curves for the allowed modes. These<br />
curves terminate on the straight lines that define the<br />
plane wave phase velocity in the core and cladding<br />
i.e., cfnl and c/n2, respectively.<br />
A narrow impulse of light, by its very nature,<br />
consists of a band of modulating frequencies and the<br />
narrower the pulse, the broader is its modulating frequency<br />
spectrum. Light at a wavelength of 1 micron in<br />
a vacuum has a frequency of 3 x 1014 Hz. If it is pulsemodulated<br />
to produce impulaes 0.1 nsec wide, their<br />
bandwidth would exceed 10 GHz (Actually 20 GHz if the<br />
Nyquist criterion is applied). The velocity of propagation<br />
of such a pulse would be defined as the velocity<br />
of the maximum of its envelope, referred to as the<br />
group velocity, Vg, which can be shown to be equal to<br />
the slope d~ld~ of the modal curves in Fig. 2.23.<br />
Since the individual frequencies, or wavelengths, making<br />
up the pulse propagate at different velocities the<br />
pulse tends to broaden and this is the source of the<br />
waveguide dispersion.<br />
Another type of dispersion or velocity variation<br />
that may affect propagation in singlemode fibers<br />
is referred to as polarization dispersion. It has not<br />
been emphasized up to this point, but in fact optical<br />
fibers operating in a so-called singlemode are in fact<br />
at least bimodal. This is due to birefringence, or
azimuthal dependence of the refractive index, i.e.,<br />
variations of the optical wave velocity, with changes<br />
in the direction of the radial component of the electric<br />
field vector. 7!his will be discussed in more detail<br />
later. The concepts are mentioned at this point<br />
because birefringence can be a source of pulse broadening<br />
and related effects in singlemode fiber due to<br />
randomly-induced transitions between different polarization<br />
atates.<br />
In cloaing this section on the various properties<br />
of optical fibers, it is appropriate to compare<br />
some of the propagation characteristics of optical fibers<br />
with thoae of more conventional waveguide communication<br />
links. This is done in graphical form in Fig.<br />
2.24. Three curves are shown that represent the attenuation<br />
of radio frequency (RF) signals with bandwidths<br />
in the frequency range from 1 MHz to 1 GHz for various<br />
widely-uaed coaxial cablea. Also shown ia the range of<br />
attenuation rates currently obtained for lightwaves,<br />
propagating in high quality fibers, that are modulated<br />
by signala over the same frequency range. For modulation<br />
frequencies above a few megahertz, optical fibera<br />
are far auperior to even the largeat diameter (> 2 cm)<br />
RG/u219 coaxial cable. Signals with a bandwidth up to<br />
1 GHz may be propagated up to fifty kilometers in highquality<br />
fibera without using repeaters (signal processors).<br />
2.2 OPTICAL FIBER FABRICATION<br />
It was indicated in Section 2.1, and shown in<br />
Fig. 2.1, that many fibera consist of a core of refractive<br />
index nl; a cylindrical cladding layer of alightly<br />
lower refractive index n2 surrounding the core, and an<br />
outer layer that serves as a protective jacket. It was<br />
1000<br />
500<br />
cient that determines the rate of the exponential<br />
decay of the core light intensity with increasing distance<br />
of travel within the core; the dispersion (pulse<br />
broadening) that depends on the differences between<br />
the propagation velocities of the various allowed modes<br />
and the variation of the modal velocities with optical<br />
wavelength; and finally the strength of the fiber that<br />
depends on how free from scratches and other imperfections<br />
the outer surface of the cladding is immediately<br />
after drawing, and on how well the cladding surface<br />
is protected during spooling, cabling, and use.<br />
This brief listing of some of the important<br />
parameters of optical fibera emphasizes the need for<br />
precise control of the refractive indices of the core<br />
and cladding.<br />
2.2.1 Refractive Index Profile Control<br />
There are several techniques being uaed by<br />
optical fiber manufacturer for maintaining preciae control<br />
of refractive index profiles and refractive index<br />
differences.<br />
A step-index fiber with a cladding of pure<br />
silica (ailicon oxide, Si02) that has a refractive index<br />
of 1.458 for a lightwave of wavelength of 0.83 ~m and<br />
that has a core of refractive index 1.461, has a numerical<br />
aperture of 0.10 as ahown in the following table:<br />
DEPENDENCE OF NUNERICAL APERTURE ON CORE INDEX<br />
SILICA CLADDING n2 = 1.458 (0.83pm)<br />
N.A. = (n12 - n22)1/2<br />
N.A.<br />
1 .:*1 0.10<br />
1.464 0.14<br />
1.469 0.18<br />
1.472 0.20<br />
When the refractive index of the core is increased to<br />
1.472, and the cladding index remains at 1.458, the<br />
numerical aperture increasea from 0.10 to 0.20 and thus<br />
changes the critical acceptance cone apex angle from<br />
11.5” to 23.0”. From the above table it may be seen<br />
that the refractive index of the core must be controlled<br />
to about one part in a thousand to obtain a desired<br />
N.A. and hence an appropriate acceptance angle to wfthin<br />
a few degrees.<br />
5<br />
3<br />
2<br />
1<br />
12 5 10 20 50 100200 5001000<br />
MODULATION BANDWIDTH (MHz)+<br />
Fig. 2.24 The variation of attenuation rate as a<br />
function of modulation bandwidth for several<br />
coaxial cables and a fiberoptic cable.<br />
T. Giallorenzi, Proc. IEEE ~, 744 (1978).<br />
alao shown that important parameters of optical fibe~a<br />
~:~)f~~, ~;~rical aperture (N.A.), equal tO (nl -<br />
is, the sine of one-half of the apex<br />
angle of the cone of light that can be injected and<br />
trapped in the core of the fiber; the radius of the<br />
core, which together with the numerical aperture, determine<br />
the modal atructure of the electromagnetic waves<br />
that may propagate in the core; the attenuation coeffi-<br />
2-12<br />
The desired refractive index of the core is<br />
usually obtained by adding varioua typea of other<br />
glasaea or dopants, to the pure silica. For example,<br />
suppose that germanium oxide (Ge02) iS added to the<br />
silicon oxide (Si02). The addition of Ge02 to Si02<br />
increases the refractive index of the mixture as ahown<br />
in Fig. 2.25a. The addition of 10 percent, by molecular<br />
content, of Ge02 to pure Si02, increases the refractive<br />
index from 1.468 to approximately 1.471.<br />
Si02 and Ge02 form glaasy (vitreoua) materials.<br />
They have microscopic molecular structures in<br />
which the moleculea are somewhat randomly distributed<br />
and disoriented rather than arranged in highly-ordered<br />
crystalline-type lattices. They have indefinite solidification<br />
temperaturea and behave aa liquida that have<br />
extremely high viscosities. Thus, under ordinary conditions,<br />
glaas fiber may be considered as consisting of<br />
super-cooled liquida. The core glaas, as diacussed<br />
above, may be considered as a mixture of two supercooled<br />
liquids, Si02 and Ge02. Their molecular density and<br />
thermal expansion coefficient are so closely matched<br />
that in the mixed state their combined structure is re-
: 1.5<br />
z<br />
o GeOz<br />
0<br />
~<br />
=1.49<br />
u<br />
w<br />
><br />
~1.48<br />
1-<br />
0 v<br />
:1.47 a<br />
L<br />
E<br />
:1.46<br />
v u<br />
,4, ~<br />
10<br />
(a) DoPANT CONCENTRATION<br />
(MOLE PERCENT)<br />
x<br />
1.49 r<br />
1.48<br />
1.47<br />
P*05<br />
1.46<br />
K<br />
1.45 ~10<br />
20 30<br />
(b) DOPANT CONCENTRATION<br />
(MOLE PERCENT)<br />
were shown as Fig. 2.12 in Section 2.1 are shown again<br />
in Fig 2.26 together with data that shows the increase<br />
in attenuation observed in fibers with various N.A.lS,<br />
obtained by adding dopants to the Si02 in the core or<br />
cladding. Dopant concentration high enough to produce<br />
numerical apertures of 0.2 or greater cause scattering<br />
and absorption leases in exceas of 10 dB/km, which is<br />
the theoretically predicted bending loss for an 0.2 N.A.<br />
fiber wound on a 3 mm radius mandrel. Thus in this respect,<br />
it may be necessary for the fiber designer and<br />
user to optimize the dopant concentration of fibers<br />
specified for a particular application.<br />
2.2.2 Fiber Fabrication Processes<br />
Fig. 2.25<br />
<<br />
f<br />
u 5 10 15<br />
K<br />
(c) DOPANT CONCENTRATION<br />
(MOLE PERCENT)<br />
The variation of the refractive index of<br />
silica glass (Si02) as a function of the<br />
concentration of various dopants.<br />
Several different methods are being used to<br />
produce fibers with particular dopant conce~trationa,<br />
gradients, and refractive-index profiles throughout the<br />
core and cladding.<br />
2.2.2.1 The Double-Crucible Process<br />
The most direct method is the double-crucible<br />
proceas. The construction of the furnace portion of a<br />
double-crucible system ia shown in Fig 2.27. The core<br />
latively strong and free of localized stresses. The<br />
addition of phosphorus pentoxide (P205) to pure silica<br />
glass (Si02) also brings about an increase in refractive<br />
index as shown in Fig. 2.25b. Thus, P205 is frequently<br />
employed as a core dopant. On the other hand,<br />
the addition of boron trioxide (B203) to pure silica<br />
(S102) produces a decrease in the refractive index as<br />
shown in Fig. 2.25c. Thus, B203 is employed as a dopant<br />
for cladding glass. The addition of dopants to pure<br />
silica, and to other glasses that are used to make optical<br />
fibers, yields the refractive indices required<br />
for the core and cladding, to produce fibers with particular<br />
numerical apertures.<br />
Large numerical apertures allow light from<br />
wide entrance angles (large acceptance angles) to be<br />
accepted into the fiber cores and still maintain total<br />
internal reflection. It was indicated in Section 2.1<br />
that bending losses are lower in fibers of higher N.A. ,<br />
so that when it is necessary to wrap fibers on small<br />
mandrels, in order to make fiberoptic sensors, it again<br />
appears to be desirable to employ fibers with as high<br />
an N.A. as is possible. Unfortunately, the addition<br />
of dopants to either the core or the cladding causes an<br />
increase in the oDtical attenuation, as shown in Fig.<br />
The attenuation versus bend “radius curves that<br />
(b)<br />
Fig. 2.27<br />
cOREF=:G-n l-cMDD’NG FEED ROD<br />
R<br />
CLADDING GLASS<br />
INNER CRUCIBLE<br />
L~<br />
TO FiBER DRAWING<br />
MACHINE WINDING DRUM<br />
IBLE<br />
The double-crucible process for optical<br />
fiber fabrication.<br />
glass is contained in the inner crucible, usually made<br />
of platinum, while the cladding glass is in the outer<br />
crucible , which is actually a cylindrical shell that<br />
surrounds the inner crucible. The two glasses are<br />
heated in such a way that they begin to flow out of the<br />
orifices at the bottom of the two crucibles as very<br />
highly ViSCOUS liquids. They then are cooled rapidly<br />
to below the solidification temperature almost immediately<br />
after they are combined in the region below the<br />
orifices. The resulting fiber is drawn under controlled<br />
tension so that its outer diameter is held nearly<br />
constant. As the fiber is drawn, the glass in the two<br />
crucibles may be maintained at a conatant level by<br />
slowly feeding rods of core and cladding-type glasses<br />
continuously into the two crucibles.<br />
A simplified overall view of a double-crucible<br />
fiber drawing system is shown in Fig. 2.28. As the<br />
fiber is drawn from the bottom of the furnace it passes<br />
.3 EK’RADIUS (mm,<br />
NIJ$.4ERICAL WE RT”RE<br />
through a non-contacting thickness gage and a feedback<br />
EFFECT OFFENDING<br />
EFFECT OF COMPOSITION<br />
system that controla the rate of rotation of the take-<br />
Fig. .26 2. The variation of attenuation in silica UP drum to maintain a constant outer diameter of the<br />
glass (Si02) optical fibers as a function cladding. The fiber then passes through a pool of the<br />
of ordinary bend radius, numerical aperture jacketing material (or materials) that coats the outside<br />
of the cladding. The fiber is then dried, cured,<br />
(N.A.), and type of dopant at a wavelength<br />
of 0.83 pm.<br />
and wound continuously on to the take-up drum.<br />
C. H. Bulmer. private communication.<br />
2-13
Fig. 2.28<br />
FURNACE—<br />
PREFORM —<br />
n<br />
II<br />
THICKNESS GAGE — - - -<br />
JACKETING UNIT z+<br />
P<br />
DRYING FURNACE —-----r!l II<br />
+<br />
TAKEUP DRUM -<br />
6)<br />
~> ‘<br />
The double-crucible optical fiber drawing<br />
system.<br />
In principle, the double-crucible process has<br />
the advantage that it may be used to draw continuous<br />
fibers of any desired length. Unfortunately, because<br />
the core and cladding glasses must be contained and<br />
heated within the crucibles, it is difficult to maintain<br />
the very high purity levels required to yield the<br />
very low-loss fibers.<br />
A much different procedure for producing extremely<br />
low-losa fibers was developed during the early<br />
and middle 1970’a. Though several variations of the<br />
same approach are being used by manufacturer, they<br />
all are based on the production of glass fiber using a<br />
vapor-phase oxidation (VPO) process.<br />
2.2.2.2 The Inside Vapor-Phase Oxidation (IVPO)<br />
Process<br />
The inside vapor-phase oxidation process<br />
(IVPO) is shown in Fig. 2.29. Vapors of various metal<br />
SiCl 4<br />
J.<br />
GeC14<br />
Q<br />
r<br />
MIXING MANIFOLD<br />
AND FLOW<br />
CONTROLLER<br />
SILICA BAIT TUBE<br />
‘+== BURNER<br />
H2+02TORCH<br />
1<br />
shown in Fig. 2.29. In each case, the halides are introduced<br />
into the mixing manifold by means of a vapor<br />
distillation process. For example, high purity oxygen<br />
may be bubbled through the liquid silicon tetrachloride<br />
(SiC14)”and germanium tetrachloride (GeC14). This process<br />
reduces the level of impurities in the halide<br />
vapors that are fed into the reaction tube. Heat is<br />
applied to the outside of the tube using a movable<br />
hydrogen-oxygen torch. This leads to oxidation of the<br />
metal halides, yielding a precipitate of very fine<br />
glass particles (soot) that builds up on the walls of<br />
the bait tube.<br />
The tube is mounted in a glass-working lathe<br />
and continuously rotated during the oxidation process<br />
so that the precipitate deposits uniformly around the<br />
inner circumference of the tube, as shown in Fig. 2.30.<br />
BAIT TUBE<br />
/<br />
REACTANTS<br />
_ SOOT FORMATION_<br />
(METAL HALIDES+ 02)<br />
SINTERED GLASS<br />
TRAVERSINiG BURNER<br />
EXHAUST<br />
:)<br />
u’<br />
SOOT DEPOSIT<br />
Fig. 2.30 The inside vapor-phase oxidation (IVPO)<br />
process for producing optical fibers.<br />
After P. Schultz, Appl. Opt. Q, 3684 (1979)<br />
The traversing burner not only provides the heat required<br />
to oxidize the various metal halide vapors but<br />
also transforms the porous soot deposit into thin<br />
sintered glass layers that are built up as the burner<br />
slowly traverses back and forth along the length of the<br />
bait tube. By controlling the concentration of the<br />
various reactants fed into the bait tube it ia possible<br />
to build up layers of Si02 glass with any desired level<br />
of doping. These will eventually form the cladding and<br />
the core of fibers that may be drawn from the resulting<br />
glass boule (preform) that is produced in this process.<br />
Several other steps are carried out before<br />
the tube is ready for fiber drawing. These are show<br />
in Fig. 2.31. After the cladding and core glasses are<br />
depoaited, the tube is heated so that under surface<br />
Fig. 2.29<br />
i)He<br />
The vapor-phase oxidation (VPO) process for<br />
producing optical fiber preforms.<br />
halides are mixed with oxygen and helium to desired<br />
highly-controlled concentration levels and fed into a<br />
hollow silica cylinder (bait tube). The chlorides of<br />
silicon and germanium exist as liquids at atmospheric<br />
pressure and room temperature, while those of phosphorus<br />
and boron must be stored under high pressure, as<br />
2-14<br />
SUSSTRATE<br />
TUBE<br />
CLADDING<br />
DEPOSITED<br />
CORE<br />
DEPOSITED<br />
COLLAPSED<br />
PREFORM<br />
Fig. 2.31<br />
c1 Q+ ,- d<br />
I<br />
/<br />
FIBER DRAWING<br />
‘1 ~ÿÿÿÿÿÿÿÿÿÿÿ<br />
@ /; SUBSTRATE REMOVED<br />
DRAWING<br />
gjjj/p”FIBER<br />
1// THIN LAYER DEPOSITED<br />
‘, //<br />
—u<br />
(3”<br />
oc’? FIBER ORAWING<br />
Stages in the processing of preforms in<br />
production of optical fibers.<br />
the
tension it collapses to eliminate the remaining center<br />
hole. In order to obtain various desired physical properties,<br />
fibers can be drawn either without removing<br />
the substrate tube, after removing the substrate tube,<br />
or after a final layer of glass haa been deposited on<br />
the outside of the collapsed preform, as shown in Fig.<br />
2.31.<br />
In the drawing process, the boule is placed<br />
in an induction furnace and fibers are drawn and coated<br />
in almost exactly the same manner as in the double-crucible<br />
technique that was shown in Fig. 2.28.<br />
2.2.2.3 The Outside Vapor-Phase Oxidation (OVPO)<br />
Process<br />
Preforms also are made by precipitating soot<br />
on the outside of a rod that is turned in a glaas-working<br />
lathe, as shown in Fig. 2.32a. In the outside vapor<br />
(a) SOOT DEPOSITION<br />
g“’+ww’””’<br />
4—.—...<br />
(b) PREFORM SISTERING<br />
o:,::.#.:~C:DING<br />
>0 INDEX n<br />
(c) FISER DRAWING<br />
Fig. 2.32 The outside vapor-phase oxidation (OVPO)<br />
process for producing optical fibers.<br />
After P. Schultz, Appl. Opt. l&, 3684 (1979).<br />
phase oxidation (OVPO) process, the core material is<br />
deposited first and then the cladding is deposited on<br />
the outside, just in the IVPO process described earlier.<br />
The amount of doping may be continuously varied during<br />
the core material deposition process. It is thus poasible<br />
to produce preforms for graded-index fibers, as<br />
well as for step-index fibers, as shown in the example<br />
of refractive index versus radial displacement curve at<br />
the extreme upper right in Fig. 2.32. The refractive<br />
index of the porous material deposited on the center<br />
bait rod decreases monotonically out to what will correspond<br />
to the core-cladding interface, and then it<br />
remains constant to the outer surface of the porous<br />
cylindrical shell.<br />
fed to the burners, a porous preform with the desired<br />
radial variation of refractive index is built up, beginning<br />
at the end of the silica rod. The rod is slowly<br />
pulled vertically upward as deposition continues at a<br />
constant rate at the lower end of the porous preform.<br />
The porous section then passes through a concentric<br />
heater ring that collapses and sinters the porous section<br />
to form a clear glass rod with the desired radial<br />
refractive index profile. The entire process is carried<br />
out inaide a reaction chamber with a carefully controlled<br />
inert atmosphere to reduce the level of impurities.<br />
The VAD process permits the production of large<br />
preforms capable of yielding single pieces of fiber<br />
over 100 km long. The optical quality of current VAD<br />
fibers is very high. Data on attenuation rates versus<br />
wavelength for VAD and IVPO fibers is shown in Fig.<br />
2.34. The IVPO process produces a fiber with a relatively<br />
large attenuation rates peak at 1.4 pm and smaller<br />
peaks in the vicinity of 1.23 pm and 0.94 Um. These<br />
are due to the vibrational mode absorption lines of the<br />
OH- radical. In the VAD process, the OH- radical contamination<br />
is reduced substantially by careful drying<br />
during the preform fabrication process thus eliminating<br />
these attenuation peaks.<br />
-..<br />
(’ ;=> STARTING SILICA ROD<br />
}! T<br />
&<br />
SiC14+BBr3<br />
f--l<br />
II<br />
TRANSPARENT PREFORM<br />
$!!$ . -- -— -. CARBONHEATER<br />
‘..-=-, .,.. .,,,,,,.,,, =..<br />
1’ I<br />
l..<br />
t<br />
I :<br />
POROIJS PREFORM<br />
+ I<br />
,..<br />
I<br />
% ~%-.+’<br />
‘\<br />
FINE GLASS PARTICLES<br />
~~•<br />
QOxy-HyDROGEN BURNERS<br />
SiC14+GeC14+PC13<br />
Fig. 2.33 The vapor axial deposition (VAD) process<br />
for producing optical fibers.<br />
After P. Schultz, Appl. Opt. l&, 3684 (19791<br />
Thus, preform fabrication by the OVPO process<br />
is a multistage procedure, including center bait rod<br />
removal, followed by porous preform sintering and the<br />
collapsing of the central hole, either prior to or during<br />
the fiber drawing process. Aa in the IVPO process,<br />
the deposition process is carried out on a glass-working<br />
lathe. Thus, the preforms produced by both processes<br />
have a limited size so that usually fiber lengths<br />
from 10 to 20 kilometers may be drawn from a single<br />
preform.<br />
2.2.2.4 The Vapor Axial Deposition (VAD) Process<br />
Length limitations are overcome in the vapor<br />
axial deposition (VAD) process that is ahown in Fig.<br />
2.33. Core and cladding glass particles ejected from<br />
oxygen-hydrogen burners are deposited longitudinally<br />
and radially on to the end of a silica rod. By carefully<br />
controlling the concentration of the metal halides<br />
2-15<br />
Fig. 2.34<br />
0.8 1.0 12 1,4 1.6 1.8<br />
WAVELENGTH (pm)<br />
The variation of attenuation as a function<br />
of wavelength in optical fibers produced by<br />
the vapor axial deposition (VAD) and the<br />
inside vapor-phase oxidation (IVPO) processes.
2.2.3 Fiber Strength<br />
The operational and shelf-life of fiberoptic<br />
sensors will depend to a large extent on the mechanical<br />
strength of the glass fibers used in them. In a certain<br />
way, glass fiber is much atronger than steel.<br />
Short, pristine silica fibers, immediately after drawing,<br />
have elastic limits, and ultimate and breaking<br />
tensile strengths, greatly exceeding that of steel<br />
wires. Stress-strain curves for priatine silica fiber<br />
and steel wire are shown in Fig. 2.35. The elaatic<br />
1 I I 1 ! , ( ! , , ,<br />
99 - *# .:<br />
80 -<br />
60 -<br />
./”<br />
./”””<br />
~ 40 - /<br />
u<br />
m<br />
3<br />
~ 20 GAGE LENGTH= 60cm<br />
if<br />
8 -<br />
4<br />
10’0<br />
- 109<br />
“E<br />
~<br />
$ 108<br />
w<br />
u<br />
G<br />
107<br />
106<br />
WIRE<br />
FIBER<br />
10–4 10–3 10–2 10–’ 10°<br />
STRAIN<br />
Fig. 2.35 Stresa versus strain curves for steel wire<br />
and pristine silica (Si02) fiber under ideal<br />
conditions.<br />
limit of steel typically uaed in wire is about 0.2 x<br />
10-9 Newtons/m2 at a atress of about 0.1 percent. Steel<br />
wires tend to break at strains of the order 0.5 percent<br />
and a stress of about 1.5x109 N/m2. On the other hand,<br />
unscratched fibers remain elastic to strains in excess<br />
of 10 percent, corresponding to stresses of about 5 x<br />
109 Newtona per square meter. However, unlike steel,<br />
which may be made malleable and capable of flow-healing<br />
small surface cracks, glass is brittle. Thus, very fine<br />
cracks in glass fibers tend to become stress concentration<br />
centers that propagate transversely across the fiber.<br />
They lead to exceasive strain and ultimately to<br />
complete rupture.<br />
A length of fiber is only as strong as its<br />
weakest section. Under constant tension a length of<br />
fiber will tend to break at its weakest point. The<br />
break will most likely occur where there is a scratch<br />
on the outer surface of the fiber. A long length of<br />
fiber ia more likely to have a weakest point that is<br />
weaker than the weakest point of a short length of<br />
fiber. Thus, fiber strength determination is a procesa<br />
of collecting statistics of failure. This is illustrated<br />
by the reaults of a seriea of tests performed on<br />
a group of test samples, each 60 cm long, cut from sections<br />
distributed uniformly along a 1 km length of fiber.<br />
Each sample was streased to rupture in a tension<br />
test machine. The percentages of the total number of<br />
specimens that failed below a given stress level are<br />
shown as a function of the breaking stress in Fig. 2.36.<br />
Fig.<br />
1 , I I , [<br />
0.5 0.8 10 2.0 3.0 4.0<br />
TENSILE STRENGTH (GN/m2)<br />
2.36 The percentage of optical fiber specimena<br />
that failed as a function of breaking tenaile<br />
strength.<br />
From the graph it may be seen that the first apecimen<br />
broke at approximately 0.5 x 109 N/m2, approximate 10<br />
percent of the specimens broke at 0.8 x 109 N/m J or<br />
leas another 10% broke at atresses between 0.8 and 1.0<br />
x 10 4N/m2, and so forth. A few of the s eclmens, however,<br />
withstood stresses of 4.0 x 109 N/m % before breaking.<br />
From a practical, application-oriented viewpoint,<br />
it is the weakest point in a length of fiber<br />
that determines ita overall strength. Thus, in specifying<br />
fibers for a given application, the maximum<br />
streas or strain to be encountered ahould be determined<br />
and the entire length of fiber to be employed should<br />
be pre-tested at some acceptable safety margin above<br />
this level. Such testing is usually done by reeling<br />
the fiber from one spool to another at a fixed rate,<br />
while maintaining the interreel section under the fixed<br />
specified stress (tension).<br />
There is evidence that preform preparation<br />
and treatment, as well aa the manner in which fibers<br />
are handled after they are drawn, contribute substantially<br />
to their overall atrength. Data on the breaking<br />
or tensile strength of a particular type of fiber drawn<br />
from identically produced preforms is shown in the bargraph<br />
in Fig. 2.37. In the upper portion of Fig. 2.37,<br />
the number of specimens versus breaking strength ia<br />
plotted for 40 specimens taken from a length of fiber<br />
drawn from an ordinarily prepared preform that was<br />
heated as usual in an RF induction furnace. As indicated,<br />
the breaking strengths ranged from approximately<br />
0.50 x 109 N/m2 to 5.5 N/m2 with a maximumof 12 specimena<br />
that broke at 3.0 x 10 4N/m2. Results are presented<br />
in the center aection of Fig. 2.37 on 46 specimens from<br />
a length of fiber drawn, using the RF induction furnace,<br />
from a preform that had been fire-polished prior<br />
to drawing in an effort to eliminate any fine cracks<br />
(microcracks) and other imperfections that might have<br />
existed in its outer surface. In this caae, the first<br />
specimen to break withstood stresses up to 1.8 x 109<br />
N/m2 and 36 of the specimens broke at a stress exceeding<br />
3.8 x 102 N/m2. In the third case, as ahown in the<br />
lower portion of Fig. 2.37, 42 specimens were tested<br />
from a fiber that waa drawn using an infrared laser to<br />
heat the preform, that also had been fire polished<br />
prior to drawing. All of the specimens withstood tensile<br />
atresses up to 4.0 x 109 N/m2 before breaking.<br />
However, instead of being distributed over a very wide<br />
range of breaking tensile strengths, the breaking points<br />
were all in the range from 4.0 to 5.25 x 109 N/m2.<br />
2-16
MAXIMUM TENSILE STRENGTH (GN/m2 = lo g N/m2)<br />
INSULATOR<br />
CONDUCTOR<br />
NO FIRE POLISH<br />
N = 40<br />
FURNACE FIRE POLISH ~<br />
N = 46 ;<br />
:<br />
10<br />
5<br />
; ~z”NDucT’oN’’NE~<br />
K<br />
Lu<br />
BAND-GAP EG<br />
—<br />
61~<br />
VALENCE BAND<br />
— —<br />
b<br />
m<br />
LASER FIRE POLISH :<br />
N = 42 ~<br />
z<br />
:L_.—dJu<br />
o 200 400 600 800 1,000<br />
P-TYPE SEMICONDUCTOR<br />
N-TYPE SEMICONDUCTOR<br />
I 1 I 1<br />
I 1<br />
DONOR LEVEL I a. a. * a. I<br />
ACCEPTOR LEVEL<br />
MAXIMUM TENSILE STRESS (KPSI)<br />
Fig. 2.37 The variation of maximum tension stress of<br />
a number of optical fibers for unpolished,<br />
furnace polished, and laser polished fibers<br />
showing the number of fibers that failed at<br />
the various stress levels in total tested<br />
for each polishing condition.<br />
These results clearly indicate how important it ia to<br />
carefully prepare the preforms and to accurately control<br />
the drawing process in order to maintain the strength<br />
of the final drawn fibers and thus get as cloae as possible<br />
to the ideal strength of silica glass.<br />
2.3 SOLID STATE <strong>FIBEROPTIC</strong> LIGHT SOURCES<br />
Solid state optical sources and detectors<br />
utilized in compact fiberoptic sensors will be discussed<br />
in this section. This information will serve as a<br />
background for understanding later discusaiona of sensor<br />
noise and packaging. In order to understand the<br />
trade-offs required, a knowledge of light production<br />
mechanisms and fabrication processes is helpful.<br />
Finally, such information is important for estimating<br />
what is likely to be available in the future.<br />
2.3.1 Energy Levels In Semiconductors<br />
Electrons in free atoms are normally tightly<br />
bound in discrete energy levels. When the atoms are<br />
located in a crystalline structure these discrete<br />
energy levels are replaced by energy bands. Some of<br />
the electrons remain tightly bound to the atom while<br />
other, more energetic electrons, have energies corresponding<br />
to the valence or conduction bands. Those in<br />
the valence band are atill localized at individual atoms<br />
but have the highest energy of such bound electrons,<br />
while electrons in the conduction band are free to move<br />
throughout the crystal. Materials can be divided into<br />
a number of classes depending on the energy gap (separation<br />
between the top energy level of the valence and<br />
the bottom energy level of the conduction band) and<br />
upon the number of electrons, if any, in the conduction<br />
band and lack of electrons in the valence band as shown<br />
in Fig. 2.38. Electrons cannot possess energies that<br />
lie in the gap.<br />
In an insulator the valence and conduction<br />
energy bands are separated by a wide energy gap. If<br />
the gaps in Fig. 2.38 were drawn to scale, the gap<br />
between the valence and conduction bands of the insulator<br />
would be much wider than that of the other materials.<br />
The conduction band in insulators is normally<br />
devoid of electrons while the valence band is filled.<br />
Therefore, when an electric field is applied across<br />
Fig . 2.38 Energy band diagrams in which the crosshatching<br />
symbolizes that there are many<br />
electrons in the various energy bands for<br />
various types of materials.<br />
the insulator, no current flows. If sufficiently high<br />
temperatures are applied (thousands of degrees) it is<br />
possible to excite some of the electrons with valence<br />
band energies up to the energy level of the conduction<br />
band. At such an elevated temperature, insulators become<br />
conductors with conduct ivities that increase with<br />
temperature. Electrical conductors, such as metals,<br />
consist of materials in which electrons fill the valence<br />
band and about half the conduction band. In this<br />
case when an electric field is applied the electrona<br />
move through the crystal easily and the material is<br />
referred to as a conductor. In metals an increaae in<br />
temperature increases lattice vibrations and electron<br />
scattering, therefore the conductivity decreases with<br />
increasing temperature. Materials with properties between<br />
insulators and conductors are known as semiconductors.<br />
Semiconductors are similar to insulators in<br />
that the valence band is filled and the conduction band<br />
is empty. However, the energy gap separating the conduction<br />
and valence bands is much smaller than that of<br />
insulators. For such semiconductors, thermal energy<br />
can excite a few electrons from the valence to the conduction<br />
band. Such materials are known as intrinaic<br />
semiconductors. Their conductivity increases with increasing<br />
temperature. By doping these materials with<br />
certain impurities, it is possible to greatly increase<br />
the number of carriers and increase the conductivity.<br />
If the dopant has carriers with an energy level that<br />
lies in the band gap just slightly below the conduction<br />
band, then thermal motions can readily excite electrona<br />
from these impurities (or dopants) into the conduction<br />
band where they are free to move through the crystal<br />
causing the material to become more conductive. Such<br />
dopants are known as donors and the resultant materials<br />
are known as negative or n-type semiconductors due to<br />
the fact that the carriers are electrons. Galium arsenide<br />
(GaAs) crystalline materials are important as roomtemperature<br />
light-emitting diodes (LED’s) and diode (or<br />
injection) lasers. In these materials, tin and tellurium<br />
serve as dopants that contribute (or donate) electrons<br />
to the conduction band while germanium (an acceptor<br />
impurity) introduces trapping sites with energy<br />
levels slightly above the valence band in the band gap<br />
itself. In the case of an acceptor, thermal motions<br />
will provide sufficient energy to permit electrons from<br />
the valence band to be trapped by an acceptor impurity<br />
atom. The holes left behind in the valence band act<br />
as positive conductors.<br />
p-type semiconductors.<br />
An important<br />
These materials are known as<br />
semiconductor energy state is<br />
2-17
shown in Fig. 2.39. This state is known as the population<br />
inversion state. It corresponds to the condition<br />
in which holes exist in the valence band and electrons<br />
exist in the conduction band simultaneously. This<br />
leads to the production of photons. The energy gap is<br />
indicated by E in Fig. 2.39. When electrons from the<br />
conduction ban~ lose some of their energy and drop down<br />
Fig. 2.39<br />
T<br />
CONDUCTION<br />
BAND<br />
+<br />
BAND-GAP,EG<br />
Q—Fc<br />
hv<br />
Fc= CONDUCTION SANO<br />
ENERGY LEVEL<br />
SPONTANEOUS: h.=EG<br />
FERMI<br />
STIMULATED: tWCEFc<br />
‘EFV<br />
PHOTONS AMPLIFY<br />
THEMSELVES<br />
Electrons (cross-hatch) from the valence<br />
band are stimulated to the energy level of<br />
the conduction band in a population inversion<br />
situation. Their return to the valence<br />
band causes the emission of photons.<br />
into the valence band they recombine with holes and<br />
photons are produced. This process is known as recombination.<br />
In the desired case, the energy is given up<br />
entirely in the form of photons. If this process occurs<br />
spontaneously, the energy of the emitted photon<br />
iS approximately equal to the band gap energy, Eg. The<br />
photons produced travel in random directions. On the<br />
other hand, if sufficient density of photons exist in<br />
the recombination region both spontaneous emission (or<br />
recombination) and stimulated recombination occur. The<br />
stimulated photons that are produced travel in the same<br />
direction as the primary photons. In the latter case<br />
the photon energy is less than the difference between<br />
the Fermi energy level in the conduction band, EFc, and<br />
the Fermi level in the valence band, EFV. These conditions,<br />
spontaneous and stimulated emission, are necessary<br />
for the proper operation of light emitting diodes<br />
(LED’S) and diode lasers, respectively. In order to<br />
understand how LED’s or diode lasers can be produced<br />
and operate in practice, consider the condition at a<br />
p-n junction as shown in Fig. 2.40. In this case, GaAs<br />
}<br />
&<br />
1%z<br />
w<br />
P<br />
-<br />
CONDUCTION BAND<br />
m<br />
I<br />
1<br />
,<br />
I<br />
, 1 I<br />
N<br />
4<br />
P-N JUNCTION<br />
Fig. 2.40 The<br />
I<br />
1:~~<br />
energy levels in a p-n junction.<br />
is doped with an acceptor material on one side of the<br />
junction, resulting in a p-type semiconductor region,<br />
and with a donor material on the other side, resulting<br />
in an n-type semiconductor region. The spatial separation<br />
between the p- and n-type regions is known as the<br />
p-n junction. The electron energy levels in the conduction<br />
and valence bands are as shown in the upper<br />
part of Fig. 2.40. Notice that when a bias voltage is<br />
not applied, as on the left, a population inversion<br />
does not occur. Electrons from the valence band of the<br />
p-type region flow into the conduction band of the n-<br />
type region until the electron energy levels on each<br />
side of the p-n junction are equal, then essentially no<br />
more electrons flow across the junction. The energy<br />
level difference across the junction constitutes a barrier<br />
to further current flow. If a forward bias voltage<br />
is applied, as shown on the right of Fig. 2.40,<br />
electrons are forced or injected into the n-type region<br />
and holes are formed in the p-type region. When the<br />
energy level of a sufficient number of electrons are<br />
raised to the energy level of the conduction band, their<br />
electron energy level exceeds the barrier energy and<br />
electrons flow across the junction into the p-region.<br />
More detail is shown in Fig. 2.41. In the population<br />
L<br />
cc<br />
1,1<br />
4, hv<br />
rFv<br />
Fig. 2.41<br />
I<br />
RECOMBINATION<br />
l-REGlON*HOMOJuNcTlON<br />
!<br />
.1 ‘ I ‘ I ~<br />
VG= EG/e<br />
FORWARD BIAS<br />
The various regions and energy levels at a<br />
forward-biased p-n junction of a semiconductor<br />
diode.<br />
inversion region, just on the left of the p-n junction,<br />
electrons can spontaneously recombine with holes producing<br />
photons. Since in this region there is a finite<br />
lifetime for the electrons depending upon the average<br />
time it takes for such recombination to occur (typically<br />
3 to 5 ns), the inversion region is restricted in<br />
spatial extent as shown in Fig. 2.41. In this case the<br />
junction is known as a homojunction and under proper<br />
conditions may be used to fabricate a homojunction LED<br />
or diode laser.<br />
Current density is directly proportional to<br />
the thickness of the recombination layer. Therefore,<br />
in order to reduce the current it is important to reduce<br />
the thickness of the recombination layer. This can<br />
be accomplished in a gallium arsenide (GaAs) crystal by<br />
the use of layers alloyed with varying amounts of aluminum<br />
(Al). The substitution of aluminum (Al. ) for gallium<br />
(Ga) occurs with little or no distortion of the<br />
crystal lattice. The energy gap plotted against the<br />
fraction of aluminum that replaces an equal fraction<br />
of gallium ( Ga) , forming gallium aluminum arsenide<br />
(GaAIAs) is shown in Fig. 2.42. For up to 37% Al substituted<br />
for Ga, the energy gap increaaes from 1.43<br />
electron-volts to 1.92 electron-volts. This is approxi-<br />
2-18
mately a 0.5 electron-volt increase. For fractional<br />
parts of Al greater than 0.37, i.e., x > 0.37, mechanisms<br />
in addition to simple photon production occur during<br />
recombination with the result that not all of the<br />
energy goes into producing photons, part of it goes into<br />
thermal energy with the possibility of crystal damage<br />
and a reduced tendency for lasing. The wavelength<br />
can be obtained from the photon energy relation E t<br />
= hf<br />
and from the wavelength-frequency-velocity relation ~f=<br />
= c/n, from which the relation 1 = hc/nEt is obtained,<br />
where h is Planck’s constant, c is the velocity of light<br />
in a vacuum, n is the refractive index taken as unity,<br />
and E t<br />
is the energy lost by a particle. For a particle<br />
with a charge of one electron that loses energy<br />
equal to the gap energy, A = 1.24/Eg, where h is the<br />
wavelength in microns and Eg is the gap energy in electron-volts.<br />
Thus for GaAs, 1 = 0.90 micron and for 37%<br />
Al, 1 = 0.64 micron. Longer wavelength lasers (1.1<br />
micron to 1.6 micron) can be produced by using the<br />
quarternary alloy iridium-gallium-arsenic-phosphorous<br />
(InGaAsP).<br />
1 P,<br />
A —P —~ qi - N—<br />
I<br />
I<br />
I<br />
I<br />
1<br />
1<br />
++++++++++++++++++++++++++<br />
I<br />
1<br />
Gal.xA~As:Ge ,~Ga l-y A’yAs ~ Gal_xAlxAs:Sn/Te<br />
I<br />
Ge ‘<br />
S;;Te<br />
Fig. 2.43 The energy levels of a semiconductor forward-biased<br />
double heterostructure laser in<br />
a junction of lower concentration alumlnum<br />
surrounded by higher concentration aluminum.<br />
‘“’~ “’:;’v:;:N:;GAp0.37COMPETING<br />
9 /.<br />
~ ,- PROCESSES OCCUR MAKING<br />
/-<br />
m2.O<br />
u ...” ONSET OF LASING LESS<br />
..0” PROBABLE<br />
n-<br />
a<br />
><br />
0 AIXGal.XAs ● FOR X INCREASING FROM<br />
OT00.37 THE REFRACTIVE<br />
%<br />
300”K<br />
z<br />
INDEX DECREASES BY 5%<br />
u.1 15<br />
[1111111111<br />
o 0.5 1.0<br />
GaAs x AIAs<br />
Fig. 2.42<br />
The band-gap energy level versus aluminum<br />
galium arsenide composition (AIXGA(l-X)AS).<br />
Another important effect is that as the fractional<br />
part of Al, x, increases from zero to 0.37 the<br />
refractive index decreases by 5%. Thus, as x increases,<br />
the energy gap increases and the refractive<br />
index decreases. The energy gap increases by almost<br />
30% and the refractive index by about 5%.<br />
The energy band structure for a crystal in<br />
which a higher concentration of aluminum in two regions<br />
sandwich a third region of lower aluminum content between<br />
them is shown in Fig. 2.43. The corresponding<br />
crystal structure can be formed by a number of processes<br />
one of which is the liquid-phase epitaxial growth<br />
process. Epitaxial growth is the growth of a crystal<br />
from the surface. For the case of interest the following<br />
is a highly simplified description. The process<br />
begins with a crystal of gallium arsenide (GaAs), one<br />
surface of which is put in contact with a high temperature<br />
solution of gallium aluminum arsenide (GaAIAs).<br />
The crystal is maintained at a slightly lower temperature<br />
than the liquid and crystal growth occurs from the<br />
surface. Once the proper thickness of this particular<br />
composition has been achieved, the crystal is removed<br />
from the bath and put in contact with another liquid<br />
having the composition corresponding to that of the<br />
next layer. A crystal results with a p-type and an n-<br />
type layer, each of which have a higher aluminum content,<br />
larger energy gap, and lower refractive index,<br />
2-19<br />
and between which is a recombination layer with lower<br />
aluminum content, smaller energy gap, and higher refractive<br />
index. The amount of aluminum in the recombination<br />
layer determines the wavelength of the light<br />
emitted. In this manner the structure corresponding to<br />
the energy diagram shown in Fig. 2.43 can be formed. By<br />
this process the recombination layer can be made thin,<br />
often as small as a few tenths of a micron. The longer-wavelength<br />
quarternary InGaAsP alloys are produced<br />
by liquid-phase epitaxial growth on an iridium phosphorus<br />
(InP) substrate.<br />
The recombination layer has lower aluminum<br />
content and therefore, a smaller energy gap, while the<br />
layers on each side have greater aluminum content and<br />
a resulting larger energy gap. In this case, when an<br />
electrical bias is applied, electrons are introduced<br />
from the n-type layer into the recombination layer.<br />
Recombination occur overwhelmingly more often in the<br />
layer with the lowest energy gap.<br />
2.3.2 Light Emitting Diodes (LEDs) and Diode<br />
Lasers<br />
The use of crystal structures to fabricate<br />
either an LED or a diode laser is shown in Fig. 2.44.<br />
Electrons are introduced into the bottom of the crystal<br />
and holes are introduced into the top. In the recombination<br />
layer, holes and electrons recombine to form<br />
photons that tend to move outward in all directions as<br />
shown on the left of Fig. 2.44. In this case, the device<br />
behaves as an LED. The light, emitted in all directions,<br />
results from spontaneous emission.<br />
In order to produce a laser it is necessary<br />
to confine and guide the emitted light. This increases<br />
the light intensity to the level where stimulated emission<br />
occurs. This is accomplished in the following<br />
way. The recombination layer has less aluminum therefore<br />
it has the lower energy gap and recombination occurs<br />
here. The use of some aluminum in the recombination<br />
layer allows the wavelength to be adjusted but in<br />
addition it reduces the probability of crystal damage.<br />
Furthermore, the layer with the smallest energy gap<br />
also has the highest refractive index. Thus, a higher<br />
refractive index layer is sandwiched between two layers<br />
of lower refractive index. This is exactly the situation<br />
that leads to lightwave trapping in optical fibers.<br />
Similarly for the structure shown on the right in Fig.<br />
2.44, photons tend to be reflected from the lower refractive<br />
index surface back into the higher-refractiveindex<br />
recombination layer. Photons are retained in the
WOTO<br />
hu=Eg<br />
LED<br />
“’SPONTANEOUS”’ RADIATON<br />
\<br />
LASER<br />
‘“STIMULATED’’RADIATION<br />
m<br />
The emitted optical power versus applied direct<br />
current is shown in Fig. 2.45. The emitted optical<br />
power initially increases linearly with current.<br />
This is the region where spontaneous emission dominates.<br />
Once a sufficiently high photon intensity level is<br />
reached, stimulated emission begins to dominate and the<br />
emitted optical power increases sharply as shown in Fig.<br />
2.45. The spontaneous emission portion of the curve is<br />
relatively temperature independent compared to the<br />
stimulated emission portion. The electrical current<br />
level corresponding to the onset of stimulated emission<br />
increases with increasing temperature, however the slope<br />
of the stimulated emission curve remains approximately<br />
constant, as shown by the T1 and T2 curves in Fig. 2.45.<br />
Thus, diode lasers are mounted on heat sinks and may<br />
require temperature control devices and feedback circuitry<br />
to control the light intensity. LED’a operate<br />
by spontaneous emission and do not require such temperature<br />
compensation. If one extrapolates backward the<br />
steeply riaing stimulated emisaion region of the curve,<br />
the intersection with the current axis, known as the<br />
threshold current, is temperature dependent. In the case<br />
shown in Fig. 2.45, the threshold current is approximately<br />
360 ma at temperature T1. Currently, diode lasers<br />
exhibit threshold currents in the range of 20 to 200 ma.<br />
The solid curve shows the optical power emitted versus<br />
current and the superimposed dots indicate repeated<br />
measurements taken after 8000 hours. As can be seen,<br />
no essential change in laser characteristics occurred.<br />
The operational lifetimes of currently manufactured<br />
diode lasers are as long as 106 hours.<br />
T2>T1<br />
Fig. 2.44<br />
The structure of a light emitting diode<br />
(LED) and a diode laser showing radiation<br />
of photons from recombination.<br />
4 -<br />
recombination region for a longer period of time by the<br />
partially reflecting mirrors that are in effect formed<br />
at the cleaved ends by the difference in refractive index<br />
between the crystal and air, as shown on the right<br />
in Fig. 2.44. Thus, photons formed in the recombination<br />
layer tend to reflect back and forth a number of<br />
times. In this process, the light intensity is increased<br />
in the recombination region. When the light intensity<br />
becomes sufficiently high, stimulated emission begins.<br />
This is the condition for lasing. When the number<br />
of energy gains matches the number of energy losses,<br />
for every photon that escapes one or more is formed<br />
within the recombination layer, thus resulting in an<br />
everincreasing recombination rate and photon production.<br />
Ultimately, equilibrium is reached and the number<br />
of photons being emitted (radiated) from the ends equals<br />
the number of photons being produced. The requirement<br />
for this to occur is that both carriers (electrons and<br />
holes) and radiation (photons) tend to be confined to<br />
the recombination layer. The carrier confinement results<br />
in the required population inversion. This insures<br />
that electron-hole recombination and the resulting<br />
photona will occur in the recombination layer. The<br />
higher refractive index in the recombination layer and<br />
the effectively partially-mirrored ends reflect or<br />
guide the photons back into the layer thus increasing<br />
the light intensity by several orders of magnitude<br />
above that of spontaneous emission.<br />
Fig. 2.45<br />
2 - SPONTANEOUS<br />
0<br />
0 100 200 300 400 500<br />
DIRECT CURRENT (mA)<br />
The optical power emitted by a diode laser<br />
as a function of applied electrical current.<br />
Diode lasers produced in the manner described<br />
above are known as double heterojunction lasers. The<br />
characteristics of such a laser are shown in Fig. 2.46.<br />
The refractive index is plotted on the left and the<br />
band gap energy is plotted on the right, both relative<br />
to the layera of the laser. The refractive index and<br />
energy gap both undergo step-function changes at the<br />
edges of the recombination layer. Other fabrication<br />
characteristics of the diode laser include the partially-mirrored<br />
ends and the electrical contacts parallel<br />
to the recombination layer. Holes and electrons are<br />
injected into the recombination region. Optical energy<br />
is distributed across the recombination<br />
approximate Gaussian distribution shown<br />
layer in the<br />
in Fig. 2.46.<br />
n<br />
)—INDEX<br />
Fig.<br />
2.46 A double-heterojunction<br />
The smaller the volume of the recombination<br />
laver the lower the reauired threshold current. As<br />
previously stated. recombination layers in double<br />
~eterojun~tion diode lasers are as thin as several<br />
tenths of a micron. However, the layer shown in Fig.<br />
2.46 extends across the entire crystal. With a recombination<br />
layer this wide, the onset of lasing does not<br />
occur uniformly throughout the layer. Lasing can start<br />
<<br />
Eg=O.3eV<br />
S~GAP<br />
ENERGY<br />
laser.<br />
2-20
I<br />
in one portion of the recombination layer but not in<br />
another. ‘Lhis is known as filamentary lasing. Such<br />
lasing behavior tends to produce noise. If the width<br />
of the layer is less than 10 microns, it is too narrow<br />
for such filamentary behavior to occur and when lasing<br />
does begin it occura uniformly throughout the layer.<br />
Furthermore, when the width is less than 15 microns<br />
singlemode propagation usually occurs. Finally, the<br />
less the width of the recombination layer the less the<br />
required threshold current. Double-heterojunction diode<br />
lasers with threshold currents as low as 20 ma have<br />
been produced. However, trade-offs may be required.<br />
For example, reducing the recombination layer width<br />
also reduces the maximum safe photon intensity. A safe<br />
cw optical power output that can be maintained without<br />
danger of facet damage is approximately 1 mW for each<br />
micron of recombination layer width. Thus, a laser with<br />
a recombination layer 10 microns wide can produce 10 mW<br />
of optical power safely.<br />
A striped-geometry injection laser diode,<br />
such as that shown in Fig. 2.47, has the desired thin<br />
and narrow recombination region. With this geometry,<br />
the emitted light spreads out in the vertical direction<br />
by as much 50” and in the horizontal by 8° or more.<br />
The dimensions of the recombination layer are of the<br />
order of 0.3 microns thick, 10 microns wide, and Up to<br />
500 microns long. These dimensions and light spreading<br />
angles must be taken into account when the laser is<br />
coupled to an optical fiber or substrate.<br />
TRANSVERSE<br />
(m)<br />
u 1<br />
Y<br />
UDINAL (q)<br />
FUNDAMENTAL MODE<br />
{ (!:;)<br />
,-I 2ndMODE<br />
,’‘ ‘,,, (m::)<br />
~<br />
E LATERAL(s)<br />
DISTANCE<br />
Fig. 2.48 The light intensity as a function of distance<br />
across the face of a laser for the<br />
fundamental and second lightwave modes generated<br />
by a laser.<br />
METAL CONTACT<br />
-’”’<br />
P<br />
(a) STRIPE CONTACT<br />
METAL CONTACT<br />
)<br />
II(Zn-DIFFUSED)<br />
/[ n<br />
P<br />
N<br />
euBsTRATE<br />
(c) DOPING-PROFILE<br />
P<br />
METAL ~ONTACT<br />
PROTON<br />
SOMSARDED<br />
(SEMI t+SULATING)<br />
METAL CONTACT<br />
‘P<br />
-4 l-+=<br />
(b) PROTON-BOMBARDMENT<br />
(d) STRIPE MESA<br />
Fig. 2.49 End views of various stripe geometry diode<br />
lasers.<br />
Fig. 2.47<br />
A GsAs-GcAIAs geometry CW injection laser<br />
diode.<br />
The distribution of optical energy across the<br />
lasing region is shown in Fig. 2.48. The fundamental<br />
and second harmonic of the longitudinal modes are shown.<br />
In the longitudinal fundamental mode, the energy tends<br />
to be concentrated more heavily towards the center, and<br />
tapers off towards the edges in a Gaussian distribution<br />
curve. If this lasing region is sufficiently wide, the<br />
second harmonic mode can occur and the emitted optical<br />
energy is concentrated in two regions.<br />
Several techniques have been employed to fabricate<br />
such stripe geometry. Some of these are shown<br />
in Fig. 2.49. The upper left (a), an oxide protective<br />
stripe is shown between the metal contact and the crystal.<br />
The stripe is formed where the oxide layer is<br />
omitted in the center. Electrons tend to be injected<br />
into this region only. In this case, the current can<br />
spread out underneath the oxide layer where it is not<br />
confined. Another technique, shown at the lower left<br />
(b), reduces such current spreading by increasing the<br />
resistivity in the regions on each side of the stripe.<br />
This can be accomplished by photon bombardment that<br />
2-21<br />
produces a semi-insulating layer on each side of the<br />
stripe. A third technique, shown at the upper right<br />
(c), uses the diffusion of a dopant, such as zinc, into<br />
the stripe region to significantly lower the resisti-<br />
Vity. Finally, almost complete electric current conf<br />
inement occurs in the structure shown at the lower<br />
right, (d). A stripe mesa (plateau or table) such as<br />
this is formed during the process of growing the crystal.<br />
Often such a mesa is buried by depositing additional<br />
material over it.<br />
For diode laser operation one major concern<br />
has been the reduction of the spontaneous emission region<br />
that was shown in Fig. 2.49. However, spontaneous<br />
emission is the mechanism responsible for light emission<br />
in LED’s. These devices are cheaper. Simpler<br />
construction techniques may be used. The light they<br />
produce is not coherent and is emitted over a much<br />
wider angle (approximately 180° ) with the result that<br />
less optical power may be coupled into a fiber. On<br />
the other hand, the spontaneous emission portion of<br />
the optical output power versus input direct current<br />
curve is far less temperature dependent than the stimulated<br />
emission region. Thus , because LED’s are less<br />
temperature dependent than diode lasers, temperature<br />
control and optical feedback problems are reduced.
LED’s are fabricated both as edge and surface<br />
emitters. An example of surface emission is shown in<br />
Fig. 2.50. A well is etched in the substrate to within<br />
EPOXY=<br />
d<br />
FIBER<br />
ELECTRICAL<br />
N<br />
CONTACT N RECOMBINATION<br />
GE~SUBSTRATE<br />
LAYER (N OR P)<br />
Fig. 2.50<br />
INSULATING<br />
/<br />
LAYER<br />
A surface-emitting LED with an etched well.<br />
approximately 1 micron of the recombination layer. This<br />
puts the surface close to the recombination layer and<br />
reduces the tendency for the light generated in the recombination<br />
layer to be reabsorbed before it can escape<br />
from the crystal. The optical fiber into which the<br />
light is being coupled is epoxied to the LED is also<br />
shown. This arrangement is satisfactory for a multimode<br />
optical fiber but, for coupling into singlemode<br />
fiber, edge emitters mounted in the same manner as<br />
diode lasers are more desirable. The waveguide character<br />
of the heterojunction structure leads to improved<br />
coupling efficiency and greater directionality, that<br />
is, it confines the emitted light to a narrower beam.<br />
In this case, the ends are cleaved at an angle several<br />
degrees from the normal to the surface of the recombination<br />
region in order to breakup optical standing waves<br />
and thus extend the region of spontaneous emission.<br />
In the discussion so far, the production of<br />
photons by electron-hole recombination has been considered.<br />
The reverse can also occur. A photon can be absorbed<br />
and thus produce an electron-hole pair. This<br />
phenomenon occurs in photodetectors and will be considered<br />
next.<br />
2.4 PHOTODETECTORS<br />
The simpleat type of photodiode is the homojunction<br />
or p-n diode as shown in Fig. 2.51. The most<br />
1<br />
>DEpLET10t4 REGloN<br />
L-<br />
1- ABSORPTION<br />
REGION -1<br />
successful photodetectors employ silicon ( Si ) although<br />
galium arsenide (GaAs) is sometimes used. When the<br />
device is reverse (back) biased as shown, the electric<br />
field is not uniform. It peaks around the p-n junction<br />
as shown the bottom of Fig. 2.51. Thus , electron-hole<br />
pairs formed by the absorption of photons in this region<br />
are swept away (depleted) , electrons going to the<br />
n side and holes to the p side. This region of increased<br />
electric field is known as the depletion region.<br />
A S shown, the depletion and absorption regions<br />
do not necessarily coincide, the absorption region<br />
tending to be larger. Electron-hole pairs, formed by<br />
the absorption of photons from the depletion region,<br />
randomly diffuse, often recombining to produce photons.<br />
A depletion region may exist even without a reverse<br />
(back) bias, but then it is narrow. However, there<br />
are circumstances where unbiased operation is important,<br />
such as for low electrical power operation. Also<br />
with a bias, a “’dark field” current (dark photocurrent)<br />
flows due to thermally generated electron-hole pairs<br />
even in the absence of light. Removing the reverse<br />
(back) bias eliminates the “dark field” current. Operation<br />
with zero bias that is, without a bias supply, is<br />
known as photovoltaic operation.<br />
In order to make the depletion region as<br />
large, or larger than, the absorption region, the arrangement<br />
shown in Fig. 2.52 is used. Here a wide re-<br />
P-REGION<br />
LIGHT<br />
3~<br />
FDEPLETIONREGIONfi<br />
INTRINSIC REGION<br />
l—ABSORPTION~<br />
REGION<br />
R<br />
1-,1~1<br />
BIAS SUPPLY<br />
b<br />
N-REGION<br />
●<br />
OUTPUT<br />
Fig . 2.52 A positive-intrinsic-negative (PIN) photodiode<br />
with bias supply.<br />
gion with little or no dopant is placed between heavily<br />
doped n-type and p-type regions on opposite ends. An<br />
undoped semiconductor is referred to as an intrinsic<br />
semiconductor, therefore the broad lightly-doped region<br />
is called the intrinsic or i-type region, or simply the<br />
i-region. Such photodiodes are known as poaitive-intrinsic-negative<br />
or PIN diodes. The corresponding electric<br />
potential curve is also shown in Fig. 2.52. The<br />
highly doped n- and p-type regions at each end have low<br />
resistivity and therefore make good electrical contact.<br />
The resistivity of the i-region is often so high that<br />
even without a reverse (back) bias the depletion region<br />
extends half way through the i-region. The voltage required<br />
to extend the depletion region completely through<br />
the i-region ia called the ‘punchthrough voltage.”<br />
Fig. 2.51<br />
The electric field and regions of a p-n<br />
(homojunction) photodiode with bias supply.<br />
When considering fiberoptic microbend sensors,<br />
reference will be made to dark field operation.<br />
A current exists in a reverse-biased photodiode even<br />
with no incident light. This current is called the<br />
dark field current and results from the thermally gen-
crated electron-hole paira that are driven by the bias<br />
voltage. Thus, the amount of dark current depends on<br />
the temperature of the photodiode, the energy gap, and<br />
the geometry of construction. Silicon photodiodes have<br />
been manufactured with very low dark currents.<br />
In order to insure that nearly all of the<br />
photons are absorbed (high quantum efficiency) the width<br />
of the i-region should exceed that of the absorption<br />
region by a factor of 2 or 3. However, the photodiode<br />
should be as thin as possible for fast response. Thus,<br />
high quantum efficiency and fast response represent design<br />
tradeoffs. Photodiodes such as those shown in Fig.<br />
2.53 are known as avalanche photodiodes (APD). Here a<br />
highly-doped layer of p-type material is sandwiched<br />
between the i- and n-regions. This results in a region<br />
of high electric field just before the positive contact.<br />
In this arrangement, an electron freed in the i-region<br />
drifts toward the positive electrode. When it enters<br />
the high field region it speeds up achieving sufficient<br />
kinetic energy to produce another electron-hole pair if<br />
it collides with the lattice. The new carriers generated<br />
in this manner can likewiae produce additional carriers.<br />
Thus, a “primary” electron freed in the i-region can<br />
free numerous “secondary” electrons in the high field<br />
region. The resultant devices exhibit high quantum efficiency.<br />
An example of one type of APD construction<br />
is shown in Fig. 2.54. The temperature dependence of<br />
APD’s is greater than that of either p-n or PIN photodiodes.<br />
hi~<br />
w<br />
kDEpLETION REGION+SECONDARY ELECTRON<br />
PRODUCTION REGION<br />
LIGHT P I P N<br />
34<br />
OUTPUT<br />
-111~+<br />
BIAS SUPPLY<br />
Fig. 2.53 Field regions in an avalanche photodiode<br />
(APD) with bias supply.<br />
v ‘k;:;;:;LL<br />
/,;;;; ,,//:: 4’, *;,<br />
P-.~<br />
A<br />
L!IGH!<br />
,,, ,;;; ::,, ,,, ,,,,,:< ,,<br />
R<br />
b OUTPUT<br />
P<br />
INTRINSIC<br />
—<br />
BIAS<br />
.—– SUPPLY<br />
+<br />
N<br />
ELECTRICAL<br />
CONTACT<br />
Fig. 2.54<br />
[<br />
r * I<br />
,’,, , ,,’ ,~,,,’,<br />
T<br />
The physical construction of an avalanche<br />
photodiode (APD).<br />
2-23
CHAPTER 3<br />
<strong>FIBEROPTIC</strong> COMPONENT INTERCONNECTION<br />
Optical power loss (attenuation) has been<br />
drastically reduced in optical fibers since 1970. A<br />
power loss of 0.2 dB per kilometer has been achieved<br />
and the prospect is good for another order of magnitude<br />
improvement to 0.02 dB per kilometer. If this occurs,<br />
approximately 50 kilometers of fiber would exhibit only<br />
a 1 dB leas. One consequenceof this progress inreducing<br />
attenuation in fiber is the increased importance of<br />
the attenuation associated with component-to-fiber,<br />
fiber-to-fiber, and fiber-to-component interconnections.<br />
Little is accomplished if 0.02 dB per kilometer<br />
attenuation is achieved in optical fibers and at the<br />
same time a number of Interconnections are required,<br />
each resulting in an appreciable fraction of a dB loss.<br />
In the case of fiberoptic sensora, where much shorter<br />
lengths of optical fiber are utilized than in communication<br />
systems, such as several hundred meters of fiber<br />
or less per sensor, and where the fiber used in most<br />
cases is not chosen for low 10SS, problems with interconnections<br />
may be less important although connection<br />
insertion losses can still be a large portion of the<br />
total loss in a fiberoptic sensor. Interconnections,<br />
especially singlemode fiber interconnections, are still<br />
required and therefore of importance. The current<br />
state of their development and manufacture will be considered<br />
in the following discussions.<br />
3.1 ‘<strong>FIBEROPTIC</strong> CONNECTORS AND SPLICES<br />
Some of the uses of interconnections in the<br />
fabrication of fiberoptic sensors include joining<br />
sources and detectors to fiber , splitting the output of<br />
a source (especially laser diodes) among a number of<br />
sensors, beam splitting and combining of light in interferometers,<br />
and providing fiber-to-fiber interconnections.<br />
All interconnections must be designed taking<br />
reflection and consequent insertion losses into account,<br />
with the aim of minimizing the insertion losses.<br />
into which light is being introduced will be designated<br />
the “sink” fiber.<br />
In connectors and splices, power losses fall<br />
into two general classes: intrinsic and extrinsic.<br />
Intrinsic losses are due to variations or imperfections<br />
in the fiber that occur during the manufacturing process<br />
and are not mechanically or externally correctable.<br />
Extrinsic losses are those that occur after the manufacturing<br />
process and are mechanically or externally<br />
correctable, such as incorrect finishing of the fiber<br />
end-surfaces or incorrect mechanical mating of fibers.<br />
Some of these effects are shown in Fig. 3.1. Only the<br />
x<br />
INTRINSIC<br />
(I:C<br />
CORE AREA MISMATCH<br />
NUMERICAL APERTURE MISMATCH<br />
PROFILE MISMATCH<br />
EXTRINSIC<br />
~ ~d<br />
-c<br />
END SEPARATION<br />
+ p’-<br />
ANGULAR MISALIGNMENT<br />
-L /<br />
t<br />
LATERAL OFFSET<br />
Fig. 3.1 Some causes of intrinsic and extrinsic<br />
power losses in optical fiber interconnections.<br />
Interconnections can be grouped into three<br />
classes, namely (1) connectors (remountable interconnections<br />
between fibers or between a fiber and some<br />
component, such’as a source, a detector, or an integrated<br />
chip), (2) splices, (fusion joints or permanent<br />
joints between two fibers or a fiber and some optical<br />
component, and (3) couplers (connections that redistribute<br />
energy between two or more fibers). In the case<br />
of singlemode fibers, splices are relatively easy to<br />
form. Splices and connectors with less than one tenth<br />
dB insertion loss per splice can be achieved. Also,<br />
in the case of singlemode couplers, especially simple<br />
four-port couplers having two input ports and two output<br />
ports, losses of less than a dB have been achieved.<br />
Multimode connectors and couplers are now commerically<br />
available and their singlemode counterparts are just<br />
beginning to become available also. In the case of<br />
multimode connectors, the average loss is about 1 or 2<br />
dB. Goals are set for less than 0.5 dB. For purposes<br />
of discussion, the fiber from which light is emerging<br />
will be designated the ‘source” fiber while the fiber<br />
3-1<br />
fiber cores are shown in these sketches. Intrinsic<br />
effects are shown on the left of Fig. 3.1. If the<br />
core areas of the source and sink fibers are not the<br />
same, the mismatch can result in a power loss. Differences<br />
in numerical aperture (NA) between the two fibers<br />
can also result in losses. For the case of graded<br />
index fibers, discussed earlier, a refractive index<br />
profile mismatch can lead to intrinsic losses. Losses<br />
occur only when directing light from a fiber of larger<br />
core or NA into a fiber of smaller core or NA. In<br />
these cases some of the light from the core of the<br />
source fiber will not be trapped in the core of the<br />
sink fiber. For the reverse, small-to-large core or<br />
NA, losses due to the mismatch do not occur.<br />
Examples of causes of extrinsic losses are<br />
shown in the right column of Fig. 3.1. If the light<br />
input to a sink fiber or output from a source fiber<br />
diverges, such as at cone angles of 15° to 20”, a core<br />
separation will allow some of the light emanating from<br />
the core of the source fiber to miss the core of the
sink fiber. Likewise angular misalignment can lead to<br />
a portion of the light from the source fiber entering<br />
the aink fiber at angles that will not allow trapping<br />
in the core. Finally, losses can occur due to lateral<br />
offset between two fibers because they are not properly<br />
aligned or their cores are not concentric with respect<br />
to the outer diameter of the fiber even when the outer<br />
surfaces of the cladding are properly aligned. In general,<br />
fibers are lined up by their outer surfaces.<br />
There are a number of other extrinsic effects that are<br />
not indicated here. The fiber end might not be smooth.<br />
‘rhis can lead to scattering loaaea. The fiber ends<br />
may not be flat cauaing lensing effects to occur. Thus,<br />
it is esaential that care be taken in the manufacture<br />
or acquisition of optical fibers, connectors, and<br />
splicea in order to inaure that the intrinaic and extrinsic<br />
leases are or can be minimized. h effect that<br />
can be corrected easily ia reflection from the ends of<br />
both fibers due to refractive index difference between<br />
glass and air. For silicon dioxide (Si02) this reaulta<br />
in a 0.4 dB loaa. In order to correct thia it is only<br />
nesaary to employ an index-matching liquid or potting<br />
material between the ends of the two fibera being buttjoined.<br />
the same fiber. For a fiber with a 50-micron core it<br />
would be necessary to hold the dimensions to + 5<br />
microns, but when dealing with singlemode fibers w~th<br />
a 5 micron core or less it is necessary to hold the diametera<br />
to within a half a micron. Differences in numerical<br />
aperature also need to be controlled accurately,<br />
however in general, refractive indices are being controlled<br />
within and among fibers to within a variation<br />
of only a few percent. Thua, the primary problem is<br />
the variation in the core diameter among fibera and<br />
within the aame fiber.<br />
The effect of the mismatch between either the<br />
core areas or the fiber numerical apertures is shown in<br />
Fig. 3.2. A problem exista when a source fiber with a<br />
1.0<br />
0.8<br />
0.6<br />
~ 0.2<br />
rn<br />
S 01<br />
~ 0.08<br />
0.06<br />
0.04<br />
0.02<br />
0.001 A I 1 1 I 1 1<br />
2 4 6 8 10 12 14<br />
PERCENT OF DIFFERENCE IN CORE DIAMETERS<br />
OR FIBERNA<br />
Fig. 3.2 Approximate losa in dB due to larger-tosmaller<br />
core diameter difference or fiber<br />
numerical aperture difference for two buttjoined<br />
optical fibers.<br />
larger core or larger numerical aperture ia joined to<br />
a aink fiber with a smaller core or a smaller numerical<br />
aperture. Furthermore, as their difference in numerical<br />
aperturea or core diameters is increased, the loss<br />
will increase. The curves in Fig. 3.2 ahow the optical<br />
power loaa in dB as a function of either the percentage<br />
difference in core diameters of larger source cores<br />
butt-joined to amaller aink corea, or source fibers<br />
with larger numerical apertures butt-joined to aink<br />
fibers with amaller numerical aperturea. These specific<br />
curves actually apply to step-index fibers but the general<br />
trenda shown are also true for graded-index fibers.<br />
A 10% mismatch in either the core diameters (larger to<br />
amaller) or the numerical aperturea (larger-to-amdler)<br />
would cauae approximately a 0.5 dB loss. For the larger<br />
multimode fibers it is not a difficult problem to maintain<br />
diameters to within 10% of each other or within<br />
3-2<br />
Fig. 3.3<br />
The extrinsic leas due to end separation for<br />
atep-index fibers is shown in Fig. 3.3. The core diab<br />
01 0.2 0.3 0.4 0.5<br />
END SEPARATION (S/D)<br />
Variation of connector power loss with endseparation-distance-to-diameter<br />
ratio between<br />
two atep-index air-gap optical fiber<br />
ends for several valuea of numerical aperture<br />
(N.A.).<br />
meter ia indicated by D and the separation by S. The<br />
coupling leas in dB is plotted as a function of S/D.<br />
This effect is alao a function of numerical aperture.<br />
The greater the numerical aperture (NA) the greater the<br />
spreading of light from the source fiber and therefore<br />
the larger the percentage of light that will miss the<br />
core of the aink fiber. In thia figure, results are<br />
plotted for NA ranging from 0.15 to 0.50. For the<br />
fibera used in fiberoptic sensora the NA of Intereat<br />
is below 0.20 and in fact more nearly 0.15. In thia<br />
case, as can be seen in Fig. 3.3, a difference of 10%<br />
in the core diameters will produce only a couple of<br />
tentha of a dB loaa. Indeed, for NA = 0.15, an end<br />
separation of half the core diameter will produce about<br />
0.7 dB coupling loaa. In the caae of aplicea there is<br />
no end separation therefore this losa does not occur.<br />
The effect of axial transverse (lateral) displacement<br />
of equal-diameter cores is ahown in Fig. 3.4.<br />
The fiber core diametera, D, and the transverse displacement,<br />
d, la shown. As can be seen, a 10% transverse<br />
displacement, which for ainglemode fibera can be<br />
0.5 urn (micron) can reault in a 0.5 dB losa. When purchasing<br />
fiber, carefully apecified fiber dimensions are<br />
important, e.g., fiber outaide diameter should be maintained<br />
uniform to ~ 1% of some nominal value and corea<br />
should be concentric to within 0.5%. For an 80 urn<br />
fiber, a 1% variation in the diameter is 0.8 pm. It<br />
could lead to a 0.4 ~m transverse displacement, which<br />
for 5 ~m core could lead to d/D = 0.08 corresponding to<br />
a leas of approximately 0.4 dB.<br />
Another extrinsic effect, an axial angular
technique is also shown in Fig. 3.6. The fiber is<br />
lightly scored and then pulled. Care must be taken so<br />
as not to bend the fiber. If the fiber bends a lip<br />
tends to form when it breaks and a smooth endface does<br />
A)STRIPJACKET<br />
B)SCORE<br />
~FILE<br />
t<br />
FIBER<br />
6 ?<br />
Fig. 3.4<br />
o 0.1 0.2 0.3 0.4 0:5<br />
TRANSVERSE DISPLACEMENT (d/D)<br />
Connector power loss due to transverse<br />
(lateral) displacement of the cores of two<br />
step-index optical fiber butt-joined enda.<br />
P<br />
C) RESULTS OFFENDING<br />
v<br />
&d<br />
h<br />
D) RESULTS OF PULLING<br />
—~.<br />
misalignment is shown in Fig. 3.5. It can occur when<br />
the fibers are not lined up axially or are not cleaved<br />
exactly at right angles to the core axes. This effect<br />
is also a function of NA, increasing as NA increases.<br />
As little as a 5° angular misalignment produces approximately<br />
a 0.4 dB loss in the connection between two<br />
fibers each with NA = 0.15.<br />
Fig. 3.6<br />
A method of cleaning an optical fiber and<br />
the results obtained.<br />
not necessarily result. An alternative approach to<br />
amooth cleaving consists of polishing the ends to provide<br />
a flat surface. This can be rather costly and”<br />
take a great deal of time. Once a smooth end has been<br />
formed, the fiber can be inserted into a connector or<br />
spliced to another fiber that alao haa a smooth end.<br />
A simple snug-fit connector is shown in Flz.<br />
3.7. A hole in- the c&nector is provided so that tie<br />
o 1“ 4<br />
~(DEGR&<br />
Fig. 3.5<br />
Connector power loss due to axial angular<br />
misalignment of the cores of two step-index<br />
optical fiber butt-joined ends.<br />
As indicated above, an important criterion<br />
for the success of either a connector or a splice is<br />
the proper end-preparation of the fibers themselves.<br />
Optical fibers used in sensors usually consist of a<br />
glass core surrounded by glass cladding that is in turn<br />
jacketed by a buffer material used to protect the surface.<br />
One type of jacket is made of acrylic material<br />
that can be removed with acetone and a swab. Another<br />
type of jacketing material consists of a IOO-micronthick<br />
layer of silicone rubber surrounded by another<br />
100- or 200-micron-thick layer of a harder plastic,<br />
such as Hytrelc. This may be removed with a razor<br />
blade. In order to prevent scratching of the fiber,<br />
the blade must be held at a very shallow angle with respect<br />
to the axis of the fiber. Furthermore, a blade<br />
should be used only once. After the jacket has been<br />
removed the fiber can be cleaved in any of several ways.<br />
One of these is shown in Fig. 3.6. Another technique<br />
consists of laying the fiber on a curved surface with<br />
approximately a 5 cm radius and applying a tension of<br />
about 1/4 pound (120 grams). The fiber is then scribed<br />
with a file causing a smooth cleave to occur. Another<br />
Fig. 3.7 A simple snug-fit connector with hole for<br />
index-matching fluid.<br />
index-matching fluid can squeeze out as the fiber ends<br />
are inserted. This is not an easily remountable type<br />
of connector. A fairly good splice can be formed in<br />
such a manner by using an index-matching epoxy in place<br />
of the index-matching liquid. If the splice is snug<br />
enough to hold the fiber fixed, an index-matching liquid<br />
can be used. The difficulty with such remountable connectors<br />
is that in order to be mounted and demounted<br />
many times it is necessary to maintain a radial clearance<br />
of at least several microns. This technique is<br />
not practical for singlemode fibers because no more<br />
than an 0.5 urn lateral displacement is allowed In order<br />
to avoid excesaive power losa.<br />
A connector, recently marketed by TRW Incorporated<br />
is shown in Fig. 3.8 (see Ref. 1 in Subsection<br />
3.1.1). Four relatively large diameter glass rods are
fused together. The ends are bent at an angle of approximately<br />
6° and the hole formed along the axis is<br />
enlarged at both ends. The fiber is factory filled<br />
with an index-matching liquid or a fluid curable with<br />
ultraviolet (UV) light. The fibers to be connected<br />
are inserted into opposite ends. The curvature causes<br />
the fibers to be pressed into the V-groove formed between<br />
two of the larger fibera thus aligning the fibers<br />
being connected as they are brought together. The resultant<br />
arrangement ia inserted into a spring loaded<br />
holding device. The resulting splices cause losses of<br />
0.02 to 0.34 dB. These may be mounted and demounted<br />
many times. If LJV-curable fluid is used they may be<br />
permanently fused.<br />
is applied and a second piece of plaatic-glass (Plexiglass)<br />
or some other flat material is placed on top to<br />
hold the fibers in position. A connector formed in<br />
this way is shown in Fig. 3.11.<br />
LENGTHWISE SECTION<br />
/ \<br />
Fig. 3.10 Joining two optical fibers using grooved<br />
plastic-glaas (Plexiglass) to form a substrate<br />
splice.<br />
Fig. 3.8<br />
A single-mode remountable optical fiber<br />
connector recently marketed by TRW Incorporated.<br />
Accurately etched V-grooves in a silicone subatrate<br />
may be used for aligning fibers. A small pressure<br />
is applied to keep them firmly seated. The use<br />
of such V-grooves to align fibers is shown in Fig. 3.9.<br />
The fibers are then welded with an electric arc. A<br />
number of fairly simple techniques may be used in the<br />
laboratory. These techniques prove to be quite effective<br />
in forming splices and remountable connectors but<br />
they are not very useful in a more permanent environment.<br />
The use of a sheet of thermoplastic material<br />
(Plexiglasc) into which a section of fiber is pressed<br />
to form a groove is shown in Fig. 3.10. An elevated<br />
temperature may be used to facilitate the process. The<br />
groove so formed is then utilized to align two aimilar<br />
fibers. An index matching liquid or potting material<br />
FI . 3.11 h optical fiber splice formed with two<br />
pieces of Plexiglasc.<br />
A fusion splice is shown in Fig. 3.12 at the<br />
OPTICAL FIBER<br />
Fig. 3.9<br />
ELECTRODE<br />
Splicing two optical fibers with an electric<br />
arc.<br />
3-4<br />
CLAD<br />
/ ~ORE<br />
— //<br />
(a) BEFORE HEATING<br />
(b) tititiING HEATING<br />
\ 4<br />
(c) AFTER HEATING<br />
x = AXIS OFFSET<br />
z<br />
o<br />
1=<br />
v<br />
Lu<br />
z<br />
o<br />
v<br />
THEORETICAL CURVE<br />
6.0<br />
/<br />
5.0<br />
+ BEFORE HEATING<br />
~ AFTER HEATING<br />
4.0<br />
1/<br />
/<br />
3.0<br />
2.0 i<br />
,/ ,’1<br />
1.0<br />
--&.-4--+”- 4<br />
0L<br />
0 0.5 1.0 1.5 2.0 2.5 3.0<br />
(x/a)<br />
Fig. 3.12 Fusion splicing of two singlemode optical<br />
fibers.<br />
Adapted from Tsuchiya and Hatakeyana, Proc. Conf.<br />
Opt. Fiber Transmission, Williamsburg, VA Feb. 1977.
left. The ends of the two fibers are brought together<br />
wittmut necessarily eliminating lateral displacement.<br />
Upon heating, the fiber melts and surface tensions tend<br />
to align the fibers as shown. The graph on the right<br />
side of Fig. 3.12 shows connector loss as a function<br />
of lateral displacement both before and after heating.<br />
The results prior to fusing is a theoretical curve with<br />
experimental reaults superimposed. As can be seen a<br />
significant reduction in loss is realized as a reault<br />
of fusion splicing.<br />
One method of connecting an optical fiber to<br />
an encased laser diode is shown in Fig. 3.13. The laser<br />
prevent damage to the mirrored faces of the laser, a<br />
alight separation must be maintained. For butt coupling,<br />
utilizing an index-matching liquid and no additional<br />
optical elementa, it is us~i to couple less<br />
than 5% of the emitted light into the fiber. From 10<br />
to 20% coupling of the light would be considered excellent.<br />
If lenaes are used to focus the light into the<br />
fiber it is possible for 70% or more of the light to<br />
be coupled into the fiber and trapped. The manner in<br />
which such a lens can be formed from the core of the<br />
fiber is shown in Fig. 3.15. In this case the core<br />
OPTICAL SPOT<br />
EMITTING SOURCE<br />
/ /1 I n<br />
Fig. 3.15<br />
Fabrication of an integral elliptical lens<br />
at the end of an optical fiber.<br />
Fig. 3.13<br />
SOURCE PACKAGE<br />
A laser-to-optical-fiber connection.<br />
surface is displaced from the fiber end because of the<br />
covering that protects the laser face. The resulting<br />
displacement between the fiber and laser source causes<br />
a great deal of the light to miss the fiber due to<br />
spreading. A lens can be used to collect the light and<br />
focus it into the core. The problem is illustrated in<br />
Fig. 3.14. At the top, the spreading (divergent) angle<br />
from the laser and the acceptance angle into the fiber<br />
are ahown. The laser emission is such that light<br />
apreads out in a 20° to 40° cone, while the acceptance<br />
angle (cone) for the fiber is 10° to 14”. Thus, even<br />
if the fiber is brought into actual contact (butt<br />
coupled) with the laser face aa shown at the bottom of<br />
Fig. 3.14, a large portion of the light being emitted<br />
will mlaa the core or go into the core at such an angle<br />
that it will be trans~tted through the core-cladding<br />
interface, into the cladding, and lost. In order to<br />
glass haa a lower glass transition (softening) temperature<br />
than the cladding. Thus, the end of the fiber can<br />
be heated and preasure applied to force a portion of<br />
the core to bulge out aa shown, forming a lens. A<br />
variety of other techniques for connecting lasers to<br />
fibers have been developed and described in technical<br />
literature. These should be reviewed In the event<br />
such an Interconnection is required.<br />
A mechanical device used to align and hold a<br />
fiber and laser is ahown in Fig 3.16. The fiber is<br />
positioned on one anvil in a V-groove and epoxied in<br />
place. The laser sets on a second anvil that also aerves<br />
as a heat aink. The two structures are brought together<br />
and the smooth faces are butted, aligned, and<br />
epoxied. A sleeve is placed over the connector. In<br />
this way a rather small fiber pigtailed laser can be<br />
formed.<br />
ELECTRICAL LEAD<br />
LASER<br />
@ ,oo--<br />
ER<br />
EMISSION PROFILEOF<br />
ALASERIN THE PLANE<br />
PERPENDICULAR TOTHE<br />
JUNCTION<br />
LASER PELLET<br />
+<br />
a.<br />
E:<br />
ACCEPTANCE CONE FORA<br />
TYPICAL STEP-INDEX FIBER<br />
FIBER<br />
LIGHT LAUNCHED ATAN ANGLE GREATER<br />
THANaWILLBE LOST<br />
CUTAWAYA<br />
Fig. 3.16<br />
3.1.1 References<br />
A pigtailed anvil for laser-to-optical<br />
ber connection.<br />
1. Fiberoptic Technology, p. 115, Dec. 1981.<br />
fi-<br />
Fig. 3.14<br />
Loas of optical power in a pigtail connection<br />
between a laser and an optical fiber.<br />
The angle = is equal to or less than the<br />
critical angle.<br />
2-5<br />
3.2 <strong>FIBEROPTIC</strong> COUPLERS<br />
It is often necessary to divide the beam emitted<br />
from a laser and insert it into two or more fibera.
A laboratory beam splitter set-up used to accomplish<br />
this is shown in Fig. 3.17. It consists of a heliumneon<br />
(HeNe) laser, a prism 3-dB divider, an objective<br />
lens to collect and focus the light into a fiber, and<br />
the associated micropositioners. The prism coupler is<br />
shown in Fig. 3.18. In order to accomplish the same<br />
purpose with a solid state device, the cores of two or<br />
more fibers must be brought sufficiently close and<br />
parallel to each other such that the energy distributed<br />
in and around one core overlaps that in the other. As<br />
shown earlier, the energy is not guided entirely in the<br />
core but tends to be guided evanescently by the cladding<br />
material itself. The cores are surrounded by a<br />
relatively thick cladding that must be removed in order<br />
to achieve coupling. After the claddings have been removed<br />
and the cores are brought close together, the<br />
degree of overlap is adjusted in order to achieve the<br />
desired coupling ratios. It is then necessary to cement<br />
or fuse the fibers together in order to fix their relative<br />
position (ruggedize) and thus to maintain the<br />
coupling ratios. The coupling ratios ahould remain con-<br />
stant with temperature.<br />
A great deal of effort is being devoted to<br />
the development of singlemode fiber couplers, particularly<br />
3-dB couplers that couple light from an input<br />
fiber equally into two output fibers. Such couplers<br />
are under development at Stanford University; the ITT<br />
Electrooptic Product Division; the Gould Research Laboratories;<br />
the U.S. Naval Research Laboratory; and the<br />
U. S. Naval Underwater Sound Center.<br />
The use of pigtailed laaers and bulk couplers<br />
can reduce volume by several orders of magnitude. Two<br />
such devices are considered next. The method developed<br />
at Stanford University is shown in Fig. 3.19. A fiber<br />
(a) EMBED (b) POLISH (c) OVERLAp<br />
Fig. 3.17<br />
A helium-neon laser with 3-dB coupler<br />
(beamsplitter) and lens in a laboratory<br />
set-up for coupling light into optical fibers.<br />
Fig. 3.19 Steps in fabricating a polished fiberoptic<br />
coupler.<br />
After Digonnet and Shaw, J. Quant. Electron, QE-18,<br />
746 (1982).<br />
is cemented into a grooved slab and the combination is<br />
then ground or polished until nearly half of the fiber<br />
is polished away virtually exposing the core. Ideally<br />
it is desirable for some cladding to remain so that the<br />
core-cladding interface is not disturbed. A coupler is<br />
formed by joining two such slabs with their faces together<br />
and adjusting the amount of overlap or alignment<br />
to achieve the desired coupling ratio. A satisfactory<br />
method of accomplishing temperature-independent fusing<br />
has not been developed.<br />
The technique developed by Sheem, et al, (see<br />
Ref. 1 in Subsection-3.2.1) is-sho~ in Fig. 3.20~ The<br />
INDEX<br />
MATCHING<br />
POTTING<br />
(b) ETCH (C) RUGGEDIZE<br />
Fig. 3.18<br />
A 3-dB priam coupler in a laboratory.<br />
Fig. 3.20<br />
Steps in<br />
coupler.<br />
fabricating an etched fiberoptic
fibers are cleaned carefully after removing the jacket.<br />
Then they are twisted together and while remaining<br />
twisted they are etched to remove most of the cladding,<br />
leaving approximately one or two microns of cladding<br />
around the core. The diameters of the fibers after<br />
etching are less than 10% of their initial diameters,<br />
therefore the resulting sections of fibers are quite<br />
fragile. The joint IS held fixed (ruggedized) by either<br />
potting in an indexmatching material or by fusing under<br />
an axial tension that prevents the fiber from sagging<br />
due to gravity and at the same time stretches the fiber<br />
slightly, thus forming a biconical taper. This is shown<br />
in Fig. 3.20 on the right. Index matching silicone<br />
liquids have been proven to be highly temperature dependent.<br />
Better results are obtained with index-matching<br />
silicone rubber. However, there is still a temperaturedependence<br />
problem. A great deal of success has been<br />
achieved recently using a gel glass material (see Ref.<br />
2 in Subsection 3.2.1) that is initially in liquid form.<br />
This material consists of metal oxides dissolved in an<br />
organic material. When heated the organic material is<br />
driven off and the metal oxides form a glass. The refractive<br />
index of the resulting glasa, and therefore<br />
the degree of coupling, can be controlled by adjusting<br />
the temperature and the length of time utilized to cure<br />
or form the gel glass.<br />
Temperature dependence can be minimized if<br />
the fibers are actually fused. The biconical taper<br />
arrangement mentioned above is shown in Fig. 3.21. To<br />
aturized bulk optical components similar to the laboratory<br />
devices shown in Figs 3.16, 3.17, and 3.18. These<br />
bulk components and fibers may be connected by various<br />
means, such as GRIN rods.<br />
Using similar techniques star couplers have<br />
been fabricated that allow the light from one fiber to<br />
be coupled equally into as many as 32 other fibers.<br />
Such devices would be useful for permitting a single<br />
optical source to simultaneously furnish optical power<br />
to a number of sensors.<br />
In summary, satisfactory techniques now exist<br />
for forming low-loss singlemode splices and remountable<br />
connectors and for fabricating low insertion loss<br />
singlemode couplers. Recently, commercially available<br />
remountable connectors have appeared on the market.<br />
Singlemode biconical tapered couplera are also becoming<br />
available. Several other types of couplers are under<br />
development by a number of groups and thus can be expected<br />
to appear on the market in the near future.<br />
3.2.1 References<br />
1.<br />
2.<br />
3.<br />
S. Sheem, Appl. Phys. Lett ~, 869 (1980).<br />
D. Tran, K. Koo, and S. Sheem, J. Quant. Electron.<br />
QE-17, 988 (1981).<br />
R. Ulrich, S. Rashleigh, ‘Beam-to-Fiber Coupling<br />
with Low Standing-Wave Rtutio”, Appl. Opt. ~, 2453<br />
(1980).<br />
END VIEW<br />
OF FIBER<br />
4.<br />
G.B. Hocker, “Unidirectional Star Coupler for Single-Fiber<br />
Distribution System”, Opt. Lett. ~, 124<br />
(1977).<br />
5.<br />
S. K. Sheem, T. G. Giallorenzi, “Single-Mode Fiber<br />
Optical Power Divider: Encapsulated Etching”, Opt.<br />
Lett. ~, 29 (1979).<br />
6.<br />
J. G. Ackerhusen, “Microlenses to Improve LED-to-<br />
Fiber Optical Coupling”, Appl. Opt. ~, 3694<br />
(1979).<br />
Fig. 3.21<br />
CROSS SECTION<br />
VIEW<br />
OF FUSED COUPLER<br />
A biconical (tapered)<br />
fiberoptic coupler.<br />
7.<br />
8.<br />
M. Saruwatari, K. Nawata, “Semiconductor Laaer to<br />
Single-Mode Fiber Coupler”, APP1. Opt. ~, 1847<br />
(1979).<br />
H. Kuwahara, N. Tokoyo, M. Sasaki, “Efficient<br />
Coupling from Semiconductor Lasers into Single-<br />
Mode Fibers with Tapered Heimspherical Ends”,<br />
Appl. Opt. g, 2578 (1980).<br />
make this coupler a portion of the cladding is removed<br />
from each of ‘the fibers. These are then twisted together<br />
and etched until the thickness of the remaining<br />
cladding is about half the core diameter. The twisted<br />
pair is then fused under some axial tension causing a<br />
decrease in diameter, especially in the region of contact,<br />
i.e., the interaction region. The original core<br />
dimensions indicated in the upper right of Fig. 3.21<br />
are reduced as shown in the lower center of Fig. 3.21.<br />
The result is that optical energy that initially was<br />
confined close to the core tends to spread into the<br />
cladding in the region where the core diameter has<br />
been decreased. This results in a stronger overlap and<br />
therefore a higher coupling ratio. The Electrooptics<br />
Product Division of ITT has recently developed a specialized<br />
optical fiber that allows them to produce<br />
fused copulers by this method without the necesaity of<br />
etching. These couplers are available for sale. An<br />
alternate to these fiber couplers is the use of mini-<br />
3.3 <strong>FIBEROPTIC</strong> CABLES<br />
3.3.1 General<br />
Just as with conventional wire interconnections<br />
and communication links, there is a need for fiberoptic<br />
cables to accomplish a number of different<br />
purposea. In many ways, the individual fibers in an<br />
optical cable are treated very much like varnished or<br />
plastic insulated copper wires. The individual fibera<br />
consist of 100- to 200-micron-OD core-cladding waveguide<br />
elements having an outer coating that may be as<br />
thin as several microns of lacquer or as thick as 200<br />
to 400 microns of plastic, such as nylon, teflon, or<br />
polypropylene. Cabling serves the purpose of spacedivision<br />
multiplexing, combining anywhere from a few to<br />
many individual fibers into a single conveniently-pack-<br />
3-7
aged multichannel unit. High-strength reinforcing members<br />
are usually added to the structure and additional<br />
inter-fiber separators (apacers) and outer protective<br />
jacketing are provided within a cable with a relatively<br />
small outer diameter. The jacket reducea the effecta<br />
of cabling and protects the individual fibers from the<br />
externl environment. Unlike copper wire and coaxial<br />
cables, crosatalk between individual fiber waveguides<br />
is virtually nonexistent. The equivalent of low resistance<br />
shorts between two wirea and ground loopa do not<br />
exist for fiber interconnection. Breaks can occur in<br />
fibers just as in wirea. However, increases in optical<br />
power loaaes in fibers due to microbend effects must be<br />
considered. These may be introduced during cable construction<br />
or installation. They also may be produced<br />
by environmental disturbance that cause differential<br />
stress or thermally induced bends. Care must be taken,<br />
in cable design to prevent such effecta, particularly<br />
when low-leas fiberoptic links are required.<br />
optic communication purpoae are shown in Fig. 3.24 and<br />
3.25. The first is an International Telephone and<br />
Telegraph cable that has a group of plastic-jacketed<br />
multimode fibers relatively looaely packed within a<br />
central polyurethane jacket surrounded by a layer of<br />
high-atrength Kevlarc fibers and an outer plastic jacket.<br />
The second is a SIECOR cable in which a group of<br />
Corning lacquer-jacketed multimode fibers are threaded<br />
loosely through individual loose fitting protective<br />
tubes that are distributed around a central steel reinforcing<br />
wire. Theae tubea are surrounded by two successive<br />
layera of Kevlarc fibers separated by inner and<br />
outer plastic jackets. In each of these two cablea,<br />
special care haa been taken to allow some flexibility<br />
and freedom of motion for the individual optical fibers<br />
to minimize the introduction of cabling-induced microbenda.<br />
3.3.2 Commercial Fiberoptic Cables<br />
POLYETHYLENE<br />
OUTER JACKE1<br />
An example of how conventional cabling procedures,<br />
developed for the communication industry for<br />
wire tranamiasion media may be employed for optical fiber<br />
cables is shown in Fig. 3.22. The figure ahows the<br />
POL<br />
FIBERS I<br />
OUTER JACKET<br />
12x12 FISER ARRAY<br />
Fig. 3.23<br />
A fiberoptic cable produced<br />
phone Laboratories.<br />
by Bell Tele-<br />
COND<br />
KEVLAR STRENGTH MEMSERS<br />
‘UTER <br />
CENT<br />
HEAVY DUTY CASLE WHICH CAN SE INSTALLEDBY REGULAR CREWS.<br />
EXTERNAL CONSTRUCTION FOLLOWS TRADITIONAL TELEPHONE CASLE PRINCIPLES<br />
Fig. 3.22 A fiberoptic cable produced by General<br />
Cable.<br />
structure of a heavy duty, combined wire and optical<br />
fiber cable manufactured by General Cable deaigned for<br />
use by the telecommunication industry. As indicated,<br />
it conaiats of two almoat identical multiwire and multifiber<br />
sandwich-like stripa that are parallel to each<br />
other on opposite sidea of a channeled plastic rod that<br />
aeparates them. The atripa are held in place with tape<br />
wrapping. l%is is surrounded by a welded aluminum tube<br />
that forms the main strengthening element of the cable,<br />
which in turn is aheathed by inner and outer plastic<br />
jacketa that encaae a corrugated steel reinforcing wrap.<br />
A aecond type of cable developed for uae in<br />
standard telephone applications is shown in Fig. 3.23.<br />
Produced by Bell Telephone Laboratories, it contains<br />
144 separate multimode fibers. Twelve fibers are fuaed<br />
in each of twelve plastic ribbona that form a 12 x 12<br />
matrix that runs through the center of the cable. This<br />
is wrapped with paper tape and surrounded by inner and<br />
outer plastic jackets aeparated by flexible fiber and<br />
steel wire strengthening elements.<br />
Fig. 3.24<br />
//<br />
;HicK PLASTIC JAcKETING<br />
A fiberoptic cable produced by International<br />
Telephone and Telegraph.<br />
LOOSE FITTING<br />
PTFE TUSES<br />
STEEL WIRE<br />
STRENGTH MEMBER<br />
Fig. 3.25<br />
KEVLAR STRENGTH<br />
MEMBERS<br />
/<br />
..’$’’.,:<br />
/’”<br />
‘y OUTER<br />
.7 JACKET<br />
k<br />
PLASTIC INNER<br />
JACKET<br />
/*w<br />
LACOUER COATED<br />
FISERS<br />
A fiberoptic cable produced by SIECOR.<br />
TWO other aimilar cables produced for fiber-<br />
3-8
Two cables manufactured in Japan by SUMITOMO<br />
for underground and indoor telecommunication applications<br />
are shown in Figs. 3.26a and 3.26b, respectively.<br />
In the cable designed for underground installations a<br />
set of four multimode fibers, separated by plastic<br />
strings are spaced uniformly around a cushioned central<br />
strength member and surrounded first by a cushioning<br />
sheath and then a second high-strength outer polyethylene<br />
jacket. This cable has an outer diameter of only<br />
18 millimeters. The multifiber cable designed for indoor<br />
test is even smaller. As shown in Fig. 3.25b, it<br />
has an outer polyvinylchloride (PVC) jacket only 8 mm<br />
in outer diameter, and an inner cushioning sheath that<br />
surrounds a set of plastic-jacketed graded-index optical<br />
fibers.<br />
used, especially for relatively short-run applications<br />
where microbend losses introduced by cabling are not<br />
excessive. For low-loss long-run applications, unique<br />
designs aimed at eliminating random bending and the<br />
effects of cabling and environmental disturbances have<br />
been developed that are capable of preventing the addition<br />
of more than 1 or 2 dB/km to the original optical<br />
power losses in the uncabled optical fibers.<br />
Discussions of fiberoptic cable risetime budgets,<br />
power budgets, bussing schemes, design parameters,<br />
environmental factors, and their use in connection with<br />
fiberoptic sensor arrays and telemetry systems is given<br />
in Chapter 6.<br />
PLASTIC STR<br />
PLASTIC TAPE<br />
ISmmOD ~ PESHEATH<br />
mO.D<br />
STRENGTHM<br />
A. underground CABLE B. INDOOR CABLE<br />
Fig. 3.26<br />
Two fiberoptic cables produced by SUMITOMO<br />
of Japan.<br />
A somewhat different cable design is employed<br />
by HITACHI to reduce losses induced by cabling and installation.<br />
As shown in Fig. 3.27, channels are formed<br />
in the outer periphery of a plastic spacer that is reinforced<br />
with a central high-strength metal or plastic<br />
tension member. The individual plastic-jacketed optical<br />
fibers, and copper wires if some are required, fit<br />
loosely in the channels and are held in by a thin outer<br />
sheath. Thus, each fiber is well isolated from both<br />
external and internal stress.<br />
CU WIRE<br />
16mm<br />
SPACER \<br />
O.D<br />
NONMETALLIC CABLE<br />
co MPOUNDCASLE<br />
Fig. 3.27<br />
A fiberoptic cable produced by HITACHI of<br />
Japan.<br />
3.3.3 Summary<br />
From the above brief discussion of current<br />
fiberoptic cabling procedures, it should be clear that<br />
in some cases conventional cabling techniques are being<br />
3-9
CHAPTER 4<br />
LIGHTWAVES IN <strong>FIBEROPTIC</strong> <strong>SENSOR</strong>S<br />
4.1 INTERFEROMRTRIC <strong>FIBEROPTIC</strong><br />
4.1.1 Intensity Interferometry<br />
4.1.1.1 Basic Principles<br />
<strong>SENSOR</strong>S<br />
The basic transduction mechanism employed in<br />
many fiberoptic sensors now being developed is the phase<br />
modulation of coherent light propagating through a section<br />
of singlemode fiber by the action of the energy<br />
field that is to be detected. The techniques of optical<br />
interferometry may be used to detect these phase<br />
shifts in lightwaves. These techniques allow for the<br />
extremely high sensitivity that is achievable with the<br />
various types of interferometric fiberoptic sensors.<br />
Until recently, optical interferometry has been a research<br />
tool used in laboratories rather than an applied<br />
or operational technique. With the development of low-<br />
10SS singlemode optical fibers, subminiature aolidstate<br />
laser light sources, photodetectors, and other<br />
related purely optical and electrooptical devices,<br />
it is now possible to construct practical interferometric-type<br />
devices for use in operational systems. Fiberoptic<br />
sensors have the potential to revolutionize sensor<br />
technology.<br />
mirror is less than the coherence length of the laser,<br />
the two beams transmitted to the detector can be made<br />
to interfere with one another. The detector output<br />
will go from a maximum to a minimum and back to a maximum<br />
each time the movable mirror is displaced by one<br />
half the optical wavelength. With this technique, it<br />
is ossible to detect mirror displacements as small as<br />
10- ? urn, e.g. 0.63 x 10-13 m, for a He-Ne laser red<br />
light.<br />
LASER<br />
SPLITTER<br />
TRANSDUCER<br />
Four different interferometric configurations<br />
currently are being employed in fiberoptic aensors.<br />
These are the Michelson, the Mach-Zehnder, the Sagnac,<br />
and the Fabry-Perot configurations. It is convenient<br />
to review their operation in terms of a nonconventional<br />
schematic arrangement using airpaths and bulk optical<br />
components before considering how they may be constructed<br />
with optical fiber elements.<br />
There is one important aspect that these interferometric<br />
sensors have in common. In each one, the<br />
output beam from an optical source is split into two or<br />
more portions. After traveling along different paths,<br />
these separate beams are recombined and allowed to actuate<br />
a photosensitive detector.<br />
4.1.1.2 The Michelson Interferometer<br />
The basic principle is illustrated first in<br />
Fig. 4.1 for the case of an air path Michelson interferometer.<br />
The beam splitter is shown as a partiallyreflective,<br />
partially-transmissive mirror. It sends one<br />
portion of the output beam from the laser upward to the<br />
fixed mirror where it is reflected back to the beam<br />
splitter, where it is then partially transmitted to the<br />
optical detector and partially reflected back toward<br />
the laaer. The other portion of the laser output beam<br />
passes through the beam aplitter, 1S reflected from<br />
the movable mirror to be partially reflected to the<br />
optical detector and partially transmitted back toward<br />
the laser. If the difference in the the path lengths<br />
back and forth to the fixed mirror and to the movable<br />
4-1<br />
4.1.1.3 The Mach-Zehnder Interferometer<br />
The Mach-Zehnder interferometer configuration<br />
is shown in Fig. 4.2. The laser output beam is split<br />
Fig. 4.2<br />
BEAM<br />
w<br />
Fig. 4.1 The principle of the Michelson interferometer.<br />
“’’R’-<br />
1<br />
BEAM<br />
SPLITTER<br />
LASER<br />
I “ ‘<br />
1 , ,<br />
MOVABLE<br />
The principle of the Mack-Zehnder interferometer.<br />
by the lower beam splitter. After traveling the upper<br />
and lower optical paths the two beams are recombined<br />
so that they may interfere with each other at the optical<br />
detector. This arrangement may also be employed to
detect displacements of the movable mirror as small as<br />
10-13 m. l%is configuration has the advantage that<br />
little or no light is fed directly back into the laser.<br />
This is in contrast to the Michelson configuration. A<br />
more detailed description of how such feedback can lead<br />
to laser instability and noise is contained in Section<br />
4.2. It should be noted that there are two other beams<br />
not shown explicitly in Fig. 4.2, that travel upward<br />
from the second beam splitter, i.e. a reflected portion<br />
of the upper horizontal beam and a transmitted portion<br />
of the righthand vertical beam. These could be fed to<br />
another optical detector to yield a second output signal<br />
, which may be employed to advantage in certain applications.<br />
4.1.1.4 The<br />
Sagnac<br />
Interferometer<br />
Fig. 4.4<br />
—<br />
1<br />
FIXED<br />
t<br />
MOVABLE<br />
MIRROR<br />
MIRROR<br />
TRANSDUCER<br />
The principle of the Fabry-Perot interferometer.<br />
The<br />
shown in Fig.<br />
Sagnac interferometric configuration is sive mirrors. The reflectivity of these mirrors usually<br />
is quite high, e.g. 95% or even higher. Assuming<br />
4.3. With this arrangement, the two porthat<br />
the reflectivity (reflection coefficient) is 95%,<br />
at any instant 95% of the output light from the laser<br />
source will be reflected back toward the laser and 5%<br />
will be transmitted into the Interferometer cavity.<br />
When this portion of the incident light reaches the<br />
right-hand mirror, 95% of it will be reflected back<br />
toward the left-hand mirror and 5% will be transmitted<br />
through to the detector. This will combine with light<br />
that has been reflected back and forth successively an<br />
increasing number of times between the two mirrors.<br />
Neglecting losses other than the 5% transmission (at<br />
each interface), each successive output beam intensity<br />
will be reduced from the previous one by the factor<br />
II<br />
II<br />
(0.95)2 = 0.9025. Assuming that the laser has a coher-<br />
) 1 11/ I A ence lenzth manv times the distance between the two<br />
mirrors, the optical signal intensity incident on the<br />
LASER<br />
I<br />
Fig. 4.3 The principle of the Sagnac interferometer.<br />
tions of the laser’s output beam are sent in opposite<br />
directions around the closed path formed by the beam<br />
splitter and the two mirrors. They are then recombined<br />
to be sent on to the photodetector and also back toward<br />
the laser. If any of the mirrors is displaced perpendicular<br />
to its reflecting surface, both path lengths<br />
would be changed by the same amount and there should<br />
be no detectable change in the interference process<br />
at the photodetector. On the other hand, if the table<br />
on which the interferometer is mounted were set into,<br />
say clockwise, rotation about an axis perpendicular<br />
to the plane of the beams, the beam traveling clockwiae,<br />
i.e. In the direction of rotation, would be<br />
delayed with respect to the counterclockwise traveling<br />
beam. The clockwise beam has to “catch up” to the end<br />
moving in the same direction. The counterclockwise beam<br />
runs into the end moving in the opposite direction.<br />
Thus, the Sagnac interferometer may be employed as a<br />
sensitive rotation detector and, in principal, it is the<br />
basis for the design of the ring laser gyroscope currently<br />
in use in a number of inertial guidance systems.<br />
4.1.<br />
tion<br />
4.4.<br />
.5 The Fabry-Perot Interferometer<br />
The fourth type of inter ferometric conf igurathe<br />
Fabry-Perot interferometer, is shown In Fig.<br />
It consists of two parallel, partially transmis-<br />
4-2<br />
detector may be found by forming the vector sum of the<br />
electric fields of the various transmitted beams.<br />
4.1.1.6 Interferometer Sensitivity<br />
The sensitivity of various interferometers is<br />
shown graphically in Fig. 4.5. Consider first, what<br />
occurs in the first three type of interferometers that<br />
were considered earlier. For the Michelson, Mach-Zehnder,<br />
and Sagnac configurations, two separate optical<br />
beams are combined at the sensitive interface of the<br />
photodetector. As indicated in the upper left, the<br />
wo electrical fields are represented by the vectors<br />
~1 and 22 which are assumed to be of equal magnitude<br />
and linearly polarized in the same direction. The optical<br />
intensit is proportional to the square of their<br />
vector sum, E z ( 8 ), which is at its maximum when the<br />
temporal and spatial relative phase angle between the<br />
two vectors is zero. If the length of one of the interferometer<br />
paths changes the phase angle varies, and<br />
E2( e ) and the intensity vary as indicated in the graph<br />
in the upper right in Fig. 4.5. , i.e. , the intensity<br />
drops to zero as 13 increases from O to n radians, varying<br />
as cos e. For further increases in e, E2( e) oscillates<br />
from zero to its maximum and back to zero again<br />
each time 13 varies by 2T radians.<br />
The corresponding diagrams for the Fabry-<br />
Perot interferometer are shown in the lower portion of<br />
Fig. 4.5. As pointed out earlier in this case, there<br />
is a set of electrical field vectors, in principle infinite<br />
in number, each successive one down from the<br />
previous by a factor R2, where R is the amplitude reflection<br />
coefficient. When the mirror separation is<br />
some integral number of half wavelengths, all of these<br />
vectors are in phase and the output intensity is at a<br />
maximum. When the separation is increased slightly,<br />
each successive vector is shifted with respect to the<br />
previous one by the same angle. By continuing the vec -
tor addition indefinitely, as indicated in the lower<br />
left, one can easily show that E2(13) in this case is a<br />
sharply peaked function with maxims at = O, Zm, 411,...<br />
and s. forth; E2(e) rapidly decreases and remains CIOSe<br />
to zero for values of f3 only slightly different from O,<br />
2n, 41r,... etc., as indicated in the vector diagram at<br />
the lower center in Fig. 4.5c. Thus, in the vicinity<br />
of its maxima, the Fabry-Perot interferometer is an extremely<br />
sensitive position and length measuring device.<br />
It is in fact, one of the most sensitive displacement<br />
measuring devices available to modern science.<br />
that are currently available, it is already possible to<br />
construct relatively small-sized, highly-stable, and<br />
quite rugged interferometric fiberoptic sensors that<br />
are capable of withstanding the rigors of many fieldtype<br />
applications.<br />
Sketches outlining “all fiber” configurations<br />
of the four different types of interferometers are<br />
shown in Fig. 4.6. In the Mach-Zehnder fiberoptic in-<br />
A) MICHELSON<br />
A) MICHELSON, MACH-ZEHNDER AND SAGNAC<br />
3dB COUPLER<br />
B) FA6Ry-pEROT<br />
El > ~<br />
A<br />
RELATIVE PHASE SHIFT (RADIANS)<br />
=;:’’:;s<br />
RTRANSDUCER<br />
B) MACH-ZEHNDER<br />
E’[@),<br />
r<br />
5’=i!4._-!=-!’=f<br />
\<br />
DISPLACEMENT- O.25 05 0.75 I MICRON<br />
C) SAGNAC<br />
LASER<br />
El<br />
DETECTOR<br />
Fig. 4.5<br />
4.1.2<br />
The sensitivity of various typea of interferometers<br />
as a function of relative phase<br />
difference between two interfering lightwavea.<br />
Fiberoptic Intenaity<br />
Interferometer<br />
Up to this point, the various interferometers<br />
have been depicted aa they exist in the typical optics<br />
laboratory, with air paths and lumped optical devices<br />
such as beam splitters and mirrora. Their extremely<br />
high displacement sensitivity has been used to measure<br />
atrain and streas. In addition, they also have a very<br />
high dynamic range. This will be brought out in more<br />
detail in later discussion. If the many advantages<br />
of the use of fiberoptic, electrooptics, and integrat -<br />
ed-optics are added, one can conceive of configurations<br />
and systems that are capable of revolutionizing sensor<br />
technology.<br />
By employing single-mode optical fibers for<br />
the interferometer paths, the rather stringent limitation<br />
on their length is immediately removed. Path<br />
lengths of the order of a kilometer are easy to achieve<br />
and are being used in practice. Extremely small, longlife,<br />
solid-state laaers and detectors that are capable<br />
of being used in hostile environments are becoming<br />
available. Elements such as etched or lapped fiber-tofiber<br />
couplers and their integrated-optic counterpart<br />
are being developed and tested. By incorporating items<br />
D) FABRY-PEROT<br />
LASER - 1 !- DETECTOR<br />
a<br />
\: ‘/<br />
PARTIAL TRANSMITTING MIRRORS<br />
Fig. 4.6<br />
The configuration of various types of fiberoptic<br />
interferometera.<br />
terferometer shown in Fig. 4.6b, the two beam splitters<br />
are replaced with two etched or lapped 3-db couplers<br />
that divide the laser output beam into two equal portions<br />
and they also recombine the light that haa traversed<br />
the two optical paths. It is possible to buttcouple<br />
the laser output beam directly into the fiber<br />
and to similarly couple the output fibers directly into<br />
the two photodetectors. Thus, between aource and detectors,<br />
the interferometera consiats only of fiber<br />
elementa. By combining integrated circuit techniques<br />
with current electrooptic capabilities, all of the other<br />
elements, including the laser, detectors, and signal<br />
processor, could be packaged in a single miniature chip<br />
to which the fibers will be butt-coupled. Though the<br />
device is not an off-the-shelf item today, there is<br />
little doubt that they will be readily available in the<br />
not too distant future.<br />
4-3<br />
4.1.3 Polarization in Fiberoptic Sensors<br />
Earlier in this discussion of interferometers<br />
it was mentioned, but not especially emphasized, that
the fiber interferometer should employ singlemode<br />
fibers. In this case, the lightwaves injected into each<br />
arm of the interferometer would propagate at a unique<br />
velocity. In fact, the so-called singlemode fibers are<br />
really at least two-mode fibers in the sense that there<br />
are two different states of optical polarization that<br />
can be propagated, i.e. the electric field vector can<br />
be resolved into two mutually perpendicular component<br />
that are perpendicular to the axis of the fiber. In<br />
an ideal, straight, imperfection-free fiber with circular<br />
symmetry, the propagation velocity is independent<br />
of the direction of polarization. Polarized light injected<br />
into such a fiber would maintain ita direction<br />
of polarization. Thus, in an interferometer application,<br />
one could have available two similarly polarized<br />
optical beams that can produce the optimum interference<br />
effects. That ia, if their intensities are equal, their<br />
electric field vectora can interfere destructively and<br />
thereby completely cancel. This can occur only for<br />
beams of the same polarization.<br />
The occurrence of such changes of polarization<br />
may be observed in the laboratory in the following<br />
situation. Referring to Fig. 4.8, imagine a beam of<br />
linearly polarized light injected into an ellipticallycored<br />
“two-mode” fiber in such a way that the input<br />
energy is aplit equally between the HEIIX and HEIIY<br />
modes. The modal velocities are different therefore<br />
the polarization state will change continuously along<br />
the length of the fiber, aa shown at the left in Fig.<br />
4.8. The HEIIX and HE1lY modes are linearly polarized<br />
along the X and Y axea, respectively, and at each position,<br />
z, along the axis of the fiber the state of polariza~ion<br />
is *determined by the time varying vector sum<br />
of Ex and ‘Y”<br />
Beginning at some point (a) where the<br />
two modes are in phase, the polarization state will<br />
change from linear polarization at (a) to circular<br />
polarization at (b); back to linear at (c), rotated,<br />
however, by 90” from its direction at (a); to circular<br />
at (d), but in the opposite direction from that at (b);<br />
back to linear at (e), just as at (a); and ao forth<br />
down the length of the ”f~ber.<br />
In reality, however, ideal fibers with perfect<br />
symmetry do not exist. The complications that<br />
this introduces can be illustrated by considering a<br />
fiber with an elliptical core, as ahown in Fig. 4.7.<br />
In this case, there will be two preferred direction<br />
of polarization, those along the major and along the<br />
minor axes of the elliptical croas section aa ahown by<br />
a and b along the x and y axes in Fig. 4.7.<br />
(a)<br />
(b)<br />
BEAT LENGTH L=;<br />
OBSERVER<br />
@(z) =(px–py)z=o<br />
—<br />
(c)<br />
t Y<br />
(d)<br />
-------——-—-——- —— z<br />
(e)<br />
Fig. 4.7<br />
I<br />
\<br />
x\<br />
b optical fiber with an elliptical cross<br />
section.<br />
Linearly polarized light injected into the<br />
fiber with its direction of polarization at some angle<br />
other than along the x or y axes will propagate in two<br />
aeparate.modea, the ao-called HE 11 and HE 11 modea,<br />
that travel at alightly different velocitie ~ . Such a<br />
fiber is aaid to have a modal birefringence, B, defined<br />
by:<br />
B= (~-~)x/211 (4.1)<br />
where the two 6’s are the propagation constanta of the<br />
two polarization modes and i is the wavelength in a<br />
vacuum. Under this condition, the direction of polarization<br />
will continuously change along the length of<br />
the fiber. Even when light that is polarized along<br />
one of the two major axes is injected into a fiber<br />
there will be some coupling into the other mode due to<br />
imperfections in the core-cladding interface, index of<br />
refraction fluctuations, and other mechanisms. Thua,<br />
both static and dynamic changes in polarization along<br />
the length of the fiber may occur.<br />
Fig. 4.8<br />
The effecta of birefringence, 6, of polarized<br />
light in an optical fiber.<br />
In this situation, if the light intensity in<br />
the core Is high enough so that the core-to-cladding<br />
scattered light ia visible to the naked eye in a darkened<br />
room, one may obaerve an apparent cyclic variation<br />
in the intensity of the acattered light along the<br />
length of the fiber, with the darker region being<br />
spaced a distance, L, apart, as shown at the right in<br />
Fig. 4.8. The darker regions correspond to aections of<br />
the fiber from which only a small amount of light is<br />
acattered towarda the eye of the obaerver. These correspond<br />
to regions where the reaultant electric field<br />
vector in the core ia parallel to the line of view, so<br />
that, from a classical electromagnetic (E&M) viewpoint,<br />
the radiation pattern of the oscillating electric vector<br />
(dipole) has a minimum in this direction. As the<br />
polarization state changea continuously in going from<br />
(a) to (c) the component of the * vector perpendicular<br />
to the line of view increases and, therefore, the<br />
light scattered toward the viewer’s eye alao increas-<br />
4-4<br />
Due to a similar pro-<br />
scattered light appears to decrease back to<br />
in the section of fiber from (c) to (e).<br />
es, reaching a maximum at (c).<br />
cesa, the<br />
a minimum<br />
ponds to<br />
2n radian<br />
The distance, L, between two minima corresa<br />
one wavelength relative shift, i.e., a<br />
phase ahift, between the HEllx and the HEIIY
modes. Since at point (a) the two electric fields are<br />
assumed to be in phase, the relative phase angle o (Az)<br />
at some distance Az displaced from (a) la given by<br />
O(AZ) = (Bx - BY)Az (4.2)<br />
Thus at (b) ~ =m/2 and at (c) @c = II and ao forth. At<br />
(e) where Az = L:<br />
o(L) = 2T (4.3)<br />
= (M-BY)L (4.4)<br />
Earlier in Eq. (4.1) the birefringence, B, was defined<br />
as:<br />
B = (BX - BY)I(2TIA) (4.5)<br />
So that for a two-mode fiber that has, at a given wavelength,<br />
A, a birefringence, B, one obtaina:<br />
L = h/B (4.6)<br />
where L la defined as the beat length.<br />
Over the distance, L, the polarization state<br />
of light propagated in a two-mode fiber may pasa through<br />
the entire cycle ahown at the left in 4.8. In terma of<br />
this process there are some applications where it is<br />
deairable to have a fiber with a long beat length, or<br />
small birefringence, B, and others for which a short<br />
beat length, or large birefringence, is preferable.<br />
For example, in the deaign of an optical<br />
fiber electric current aensor employing the Faraday effect<br />
as the transduction mechanism, a relatively ahort<br />
fiber element may be employed and a long beat length,<br />
L, is preferable. When attempting to detect magnetically-induced<br />
birefringence, any slight changes in a<br />
large inherent birefringence, B, i.e., small L, might<br />
maak the polarization changea induced by the magnetic<br />
fielda associated with the electric current under measurement.<br />
In certain applications of interferometrictype<br />
sensora, “two-mode” fibers with high birefringence,<br />
and short beat lengtha can be uaed to advantage. As<br />
already indicated, the output beams from the two patha<br />
of the interferometer not only must be equal in amplitude<br />
but alao polarized in the same direction if they<br />
are to totally cancel one another when they are out of<br />
phaae by~ radians. In many interferometer sensor applications<br />
fiber path lengtha of aeveral tens to aeveral<br />
hundreds of metera are employed. It is irnpoaaible<br />
to draw perfect fibers without variations and fluctuations<br />
in core dimensions and refractive indices, and<br />
without core-cladding interface ripplea. Therefore,<br />
even when the direction of polarization of the injected<br />
light la along one of the preferred axes in an elliptical<br />
fiber, there will be at least random coupling due<br />
to auch perturbations. Thus, as the propagation distance<br />
increases, light originally in the HEIIX mode, ia<br />
transferred into the HE1lY mnde. If the birefringence,<br />
B, is different from zero, (even if it only fluctuates),<br />
there will be some changes in the direction of polarization<br />
and theae could reault in a reduction in the detection<br />
sensitivity of the interferometer.<br />
One method of improving detection sensitivity<br />
is to employ fibers that have high birefringence and<br />
short beat lengtha. In this case, due to the large difference<br />
in the electric field profilea associated with<br />
the HE1lX and HE ~y modes, the probability that a given<br />
perturbation wil 1 cauae a transition between modea la<br />
much lower than in the case of a fiber with amall birefringence,<br />
B. In this senae, a high B fiber is a polarization-maintaining<br />
fiber and therefore may be uaed to<br />
advantage in Interferometric-type senaors.<br />
One way in which a high-birefringence fiber<br />
may be made is shown in Fig. 4.9. At the left an<br />
~] (,3J)<br />
/“n\<br />
~cQER<br />
IDEAL FIBER \ /<br />
PREFORM<br />
Fig. 4.9 The production of high birefringence optical<br />
fibera.<br />
idealized fiber having a rectangular core and cladding<br />
structure is shown. Ita bimodal structure can be reprepresented<br />
as the sum of two planar waveguide modes,<br />
one where the height of the core croas section is the<br />
determining factor and the other where the length of<br />
the core croaa aection la the determining factor. These<br />
modes would have substantially different propagation<br />
constants and the B value would be large.<br />
Several approaches have been taken to produce<br />
fibers that approximate this ideal atructure. One<br />
technique is shown at the center of Fig. 4.9. A preform<br />
is produced consisting of a circular core and a<br />
two-layered circular cladding. The dotted line in the<br />
figure la the outline of its original outer circumference.<br />
Large semi-circular segments of the outer cladding<br />
along the length of the preform are removed aa<br />
indicated and then two additional slots are cut to<br />
expoae a section of the inner cladding. Thia element<br />
is then heated until, under the action of surface tension,<br />
it returns to a circular croaa section. The core<br />
and inner cladding each aasume an elliptical ahape.<br />
Fibera are then pulled from this modified preform. The<br />
reaulting fibers have relatively large birefringence, B.<br />
4.2 PHASE AND INTENSITY DETECTION<br />
4.2.1 Phase Detection<br />
As will be ahown, phaae modulation will be<br />
converted to amplitude modulation prior to detection.<br />
Thus, it is useful to first conaider the procesa involved<br />
in amplitude modulation. An optical source input,<br />
Iin, into an intensity-type aenaor la ahown in<br />
Fig. 4.10. A graph of the optical input to the sensor<br />
versus time is shown at the bottom left. In the aensor,<br />
a baseband input signal, Sb, amplitude modulatea<br />
the optical aource input, Iin, to produce the output<br />
signal from the sensor aa ahown in the graph at the<br />
bottom center. Finally, the amplitude-modulated optical<br />
output signal from the aenaor is photodetected resulting<br />
in an amplitude-modulated electrical output<br />
aignal from the photodetector aa ahown at top and bottom<br />
right of Fig. 4.10. Phaae modulation cannot be<br />
directly detected due to the fact that the light frequency<br />
is approximately 1014 Hz. Photodetectors are<br />
unable to respond to such high frequencies, i.e., they<br />
4-5
I<br />
1<br />
cannot follow the inatantaneoua valuea of such highfrequency<br />
variations. Thus , in order to accomplish<br />
phase detection, an interferometric technique must be<br />
uaed to convert the phase modulation to amplitude modulation<br />
prior to detection.<br />
OPTICAL<br />
SOURCE<br />
IIN<br />
sb<br />
t<br />
<strong>SENSOR</strong><br />
‘OUT<br />
OPTICAL<br />
DETECTOR<br />
ikiki&<br />
T IME TIME TIME<br />
Fig. 4.10<br />
‘OUT<br />
Input-output relations in an intenaity-type<br />
fiberoptic senaor.<br />
The phaae angle, $, measured with reference<br />
to the plane of entry into a fiber, of a lightwave of<br />
wavelength A in a fiber of length L ia given by:<br />
4 = 2nL/i = 2mIlL/lo (4.7)<br />
where A. la the wavelength of light in vacuum and nl la<br />
the refractive index of the fiber core. If L and X. are<br />
expresaed in the same units, $ will be in radians. If<br />
the fiber undergoes a change in length, AL, relative to<br />
the fixed plane of entry, the phase angle at the end<br />
plane of the fiber becomes:<br />
$+A41=2ml(L+AL)/~ (4.8)<br />
These two caaea are shown in Fig. 4.11. An assumption<br />
is made here that the value of nl does not change<br />
throughout the fiber during its change in length. While<br />
this is not true, it will be approximately true in many<br />
of the caaes to be considered later.<br />
Consider the situation in which there are two<br />
optical fibers, one located in each of the two arms of<br />
an interferometer. A lightwave is simultaneously introduced<br />
into the left ends of these two fibera, initially<br />
of the same length or differing in length by an integral<br />
multiple of 2TT rad. Assume the upper fiber in Fig.<br />
4.11. is the reference fiber. Consider the case in<br />
which the output of the two fibers is initially in phase<br />
and when combined interfere constructively. If the<br />
length of the lower fiber increases due to an applied<br />
stress or a thermal change, the output intenaity of the<br />
interferometer will decrease, reaching a minimum when<br />
the length of the lower fiber haa increased by A/2,<br />
i.e., T rad. At this point if the lower fiber continuea<br />
to change, then the output amplitude will increase,<br />
returning to ita maximum value when the length of the<br />
lower fiber has increased by another i/2, i.e., m rad.<br />
The reaulting current out of a photodetector placed at<br />
the end of the fibera is shown in the upper curve of<br />
Fig. 4.12. The ordinate is the photodetector current<br />
lr<br />
o+ZD‘--–-–– ‘- ‘MAX<br />
:+<br />
~~<br />
SE<br />
~ > .- –-– - - - - - - - - - - - TMIN<br />
Ov<br />
30 ~<br />
Fig. 4.12<br />
2% 37r<br />
L+(RAOIANS)<br />
A+4RAOIANS)<br />
● PHASE DRIFT CAUSES PtiOTO -<br />
DETECTOR CURRENT (i) TO VARY<br />
❑ ETWEEN TM,N AND IMAX (FADING)<br />
● PHASE SENSITIVITY -d,ld(A.$)<br />
● MAXIMUM SENSITIVITY FOR<br />
A+=V2 ,3v~<br />
● V2 PHASE BIAS REIIJIREO FOR<br />
MAXIMUM SENSITIVITY (QUADRATURE<br />
CONDITION)<br />
Photodetector output current and its derivative<br />
resulting from lightwave phasechange<br />
fiberoptic sensor output.<br />
o<br />
+0<br />
t<br />
FIBER<br />
CORE<br />
0<br />
i<br />
+=<br />
?<br />
27r LENGTH 2%nL<br />
.— 1<br />
WAVELENGTH A I<br />
+0 -A++<br />
++A~= —(L+ 2un AL)<br />
A<br />
Fig. 4.11 Phase change of a lightwave through an optical<br />
fiber of original length L that has<br />
been stretched by a length AL.<br />
L<br />
and the abscissa is the difference in phase between the<br />
lightwaves in the two arms. This output ia typical of<br />
the effect of a phaae drift (shift) aaaociated with the<br />
return to thermal equilibrium following a step function<br />
increase in temperature. In general, such oscillations<br />
are undesirable especially when the signal being measured<br />
produces phase changea many orders of magnitude<br />
smaller. A case where such oscillations are a measure<br />
of the signal being detected is described below.<br />
A simple technique for meaauring the rate of<br />
change of presaure for large presaure changes ia ahown<br />
in Fig. 4.13. The sensing element consista of a length<br />
of fiber, L, tightly (prestressed) wound on a mandrel<br />
of a compliant material such aa Teflonc. The pressure<br />
may be applied either to the outside of the fibermandrel<br />
combination or, for the caae of a hollow mandrel<br />
to the inside. Aa the length of fiber in the senaing<br />
arm changes the output of the photodetector will<br />
sweep through maxima and minima as ahown by the upper<br />
curve in Fig. 4.12. The time rate of change of pressure<br />
can be related to the frequency of oscillation in a<br />
atraight forward manner. The number of oscillations per<br />
unit time is proportional to the change in fiber length<br />
per unit time, where the change in length is expreased<br />
4-6
as a number of wavelengths. An expression for the frequency<br />
can therefore be obtained by dividing the change<br />
in the fiber length per unit time by the wavelength of<br />
light. This is given by the expression:<br />
Where lo/nl<br />
f= (nl/Ao)(dL/dt) (4.9)<br />
is the wavelength in the fiber core.<br />
From the expression for the volume of the<br />
mandrel, V = rr2D, it follows that:<br />
~V/V = 2Ar/r + AD/D (4.10)<br />
where r and D are the radius and length of the mandrel<br />
respectively. For hydrostatic pressure AD/D . ~r/r and<br />
Eq. (4.10) becomes:<br />
The compreaaibility,<br />
can be written:<br />
AV/V = 3Ar/r. (4.11)<br />
K = (1/V)(dV/dP), of the mandrel<br />
K = (3/r)(dr/dP). (4.12)<br />
Since for a compliant mandrel, the change in fiber<br />
length is cauaed primarily by the change in r, where<br />
L = 2nNr, it follows that:<br />
to 5 x 104 atmoslsec). Assuming the maximum counting<br />
error is one cycle, the maximum error will range from<br />
1% at the loweat rate of change to 10-4% at the highest.<br />
The time rate of change of pressure versus frequency<br />
is given in Fig. 4.14 for various lengths of fiber.<br />
For lengths as short aa 0.1 m a significant error<br />
will ariae due to the uncertainty in the number of<br />
turns. This source of error will decrease as the number<br />
of turna increases.<br />
LASER<br />
BC<br />
n<br />
PRESSURE APPLIED<br />
TO MANDRELTO<br />
CHANGE THE<br />
LENGTH OF FIBER<br />
I<br />
R<strong>SENSOR</strong><br />
59 ‘ANDRE’<br />
1!BC<br />
L# u PHOTODETECTORS<br />
)<br />
(1/L)(dL/dp) = (1/r)(dr/dP) (4.13)<br />
and substituting Eq. (4.13) into Eq. (4.12) yields:<br />
Letting:<br />
K = (3/L)(dL/dP). (4.14)<br />
Fig. 4.13<br />
A homodyne Mach-Zehnder-type interferometer<br />
detection aystem.<br />
in Eq.<br />
dL/dP = (dL/dt)(dt/dP) (4.15)<br />
(4.14) and solving for (dP/dt) results in:<br />
,.3<br />
dP/dt = (LK/3)/(dL/dt). (4.16)<br />
Finally, substituting Eq. (4.9) into Eq. (4.16) yielda<br />
the deaired expression for the time rate of change of<br />
pressure in terms of the frequency of oacillationa:<br />
~<br />
co<br />
,.2 -<br />
dPldt = (3Ao/KLnl)f. (4.17)<br />
The quantity on the right multiplying f is the acale<br />
factor. Since the length of fiber, L, is very much<br />
greater than the expected change in length, the scale<br />
factor remains approximately constant. (A stress of<br />
100 Kpsi is required to produce a one percent change in<br />
fiber length.) For large changea in pressure the values<br />
of Kand nl also vary, but in oppoaite directions. The<br />
scale factor in Eq. (4.17) can be changed by employing<br />
a mandrel exhibiting a different sensitivity. In general,<br />
however, the largest changea in acale factor can<br />
be accomplished by changing the length of fiber. Care<br />
must be taken to inaure that the mandrel doea not exhibit<br />
resonant frequencies which are excited by transients<br />
associated with the time rate of change of pressure.<br />
Such resonances may constitute the upper limit<br />
of measurements.<br />
Choosing ~<br />
Si02, and for Teflon?<br />
= 0.85 X 10<br />
K .3.6 x ;:-iT’cm3)d;:”;;e&<br />
dP/dt = 4.85 x 105 f/L (pascala/aec). (4.18)<br />
l%us for 1 m < L < 100 m and 100 Hz < f < 10 kHz, the<br />
time rate of change of pressure detected will vary between<br />
5 x 105 palaec and 5 x 109 pa/see (5 atmos/sec<br />
~<br />
~<br />
= 100 -<br />
a<br />
v<br />
1(J’<br />
Icrz<br />
,.2<br />
103 104<br />
OUTPUT FREQUENCY (Iiz)<br />
Fig. 4.14 Relation between time rate of change of<br />
pressure and frequency for varioua lengths<br />
of optical fiber.<br />
The above derivation assumed hydrostatic<br />
pressure. Thua, the change in preasure acrosa the sensor<br />
muat be smell compared to the rate of change being<br />
measured. For a senaor whose dimension along the direction<br />
of propagation ia 3 cm, and assuming the velocity<br />
of propagation for sound at high pressure or for a shock<br />
wave to be 3000 mlaec, the pressure differential acroas<br />
the sensing element will be 0.5 atmos, or one part in<br />
105 of the pressure change being measured.<br />
4-7
Next consider the other extreme: the detection<br />
of changes in length (or more exactly, phase) very<br />
much smaller than a wavelength, such as 10-6 radians.<br />
Any large amplitude drift (change) greatly increases<br />
the difficulty of measuring small changes. The signal<br />
to be considered will appear as a small amplitude perturbation<br />
as was shown on the upper curve in Fig. 4.15.<br />
The sensitivity to phase changes varies as the slope<br />
of this curve. Thus, the lower curve, obtained by taking<br />
the derivative of the photodetector output with<br />
respect to$ is the phase sensitivity for amall amplitude<br />
changes. The maximum sensitivity occurs for odd<br />
multiples of T/2 while zero sensitivity occurs for even<br />
multiples of n/2. This is shown in Fig. 4.15. Here the<br />
photodiode current is plotted against the bias (phase)<br />
angle. In order to demonstrate the sensitivity, a cw<br />
(sinusoidal) signal of amplitude ~ 10” (electrical degrees)<br />
is superimposed about a bias (quiescent or op-<br />
+<br />
5<br />
K<br />
lx<br />
a<br />
U<br />
8<br />
s<br />
6<br />
1<br />
L<br />
I<br />
I<br />
I<br />
----=-.—.—<br />
I >\<br />
PHASE VARIATION<br />
I<br />
-20 0 20 40 60 80<br />
BIAS ANGLE(”)<br />
CURRENT OUT<br />
II<br />
Fig. 4.15 Sensitivity of fiberoptic<br />
at O“ and 90° bias angle.<br />
100 120 140<br />
homodyne sensor<br />
crating) point at O“ and at 90”. The amplitude of the<br />
resulting output current is obtained by projecting the<br />
phase oscillation (input signal) upward on to the solid<br />
curve graphically and plotting the resulting output current<br />
about a horizontal line as is normally done graphically<br />
with any transfer function. At 90° the resulting<br />
current is large and of the same frequency as the input<br />
signal. At O“ bias however the amplitude of the photodetector<br />
current is small and exhibits a frequency twice<br />
the excitation frequency because oscillation is on both<br />
sides of the maximum. Thus, consider such a signal initially<br />
at the 90” bias point. Now for the magnitude of<br />
input signal shown in Fig. 4.15, if the 90” relative<br />
phase between the two arms of the interferometer drifts<br />
toward the 0° point, the amplitude of the photodetector<br />
current would decrease, and at leas than 10° biaa a<br />
second harmonic would appear. The current amplitude<br />
would become minimum at 0° bias at which point the fundamental<br />
component will have become zero with only a<br />
small second harmonic left. This process is referred to<br />
as fading. The 90” bias condition is known as quadrature.<br />
l%is mode of detection is called homodyne detection.<br />
4.2.2 Homodyne Detection Applications<br />
As pointed out in the discussion above, homodyne<br />
detection requires quadrature operation and in addition<br />
some means of compensating for large amplitude<br />
4-8<br />
drift. In addition laser noise reduction will be shown<br />
to be necessary.<br />
A schematic of the Mach-Zehnder fiberoptic<br />
interferometer using phase-locked homodyne detection is<br />
shown in Fig. 4.16. The light in the laser beam is<br />
3dS COUPLER<br />
REFERENCE ARM<br />
SENSING ARM<br />
/<br />
OUTPUT HIGH PASS<br />
-SIGNAL<br />
SIGNAL“4+ F ILT ER $p<br />
K(<br />
LOW PASS<br />
I<br />
SIGNAL & NOISE<br />
FILTER<br />
3CU3COUPLER<br />
Fig. 4.16<br />
AMPLIFIER<br />
& SUMMER<br />
ePHOTODIODES<br />
A Mach-Zehnder fiberoptic interferometer<br />
employing phase-locked homodyne detection.<br />
split by the 3-dB coupler into the two arms of the interferometer.<br />
The arm on the right is taken to be the<br />
signal arm and the arm on the left is taken to be the<br />
reference arm. The latter contains the phase shifter<br />
described below. The light through the two arms is recombined<br />
by the lower 3-dB coupler that converts the<br />
phase modulation to an intensity modulation. The two<br />
optical outputs of the 3-dB coupler are each photodetected.<br />
The electrical outputs of the two photodetectors<br />
are fed into a differential amplifier. It in turn<br />
feeds the compensator circuit. The compensator circuit<br />
provides an output signal, the signal required for the<br />
phase shifter, and a reset signal. A detailed discussion<br />
is given in the next subsection.<br />
There are many types of laser noise, such as<br />
phase noise, amplitude noise, and noise due to multimode<br />
and satellite mode operation. This is especially<br />
important when the source is a diode laser that is<br />
closely coupled to a fiber.<br />
4.2.3 Phase Noise<br />
The output noise of the interferometer in dBV<br />
as a function of path length difference between the two<br />
arms of the interferometer expressed in millimeters is<br />
shown in Fig. 4.17. The system noise determines the<br />
minimum detectable phaae shift. The minimum detectable<br />
phase shift, measured in a 1 Hz bandwidth, is shown<br />
plotted in radians using the ordinate scale on the<br />
right in Fig. 4.17 (see Ref. 1 in Subsection 4.2.8).<br />
Experimental data is given for 50 Hz, 500 Hz and 2 kHz.<br />
The interferometer was operated in quadrature. On the<br />
log acales used, a straight line plot of decreasing<br />
noise at each frequency is obtained as the path length<br />
is reduced. Notice that varying the path length from 1<br />
mm to 1000 mm, that is, to 1 meter, results in a 60 dB<br />
increase in output noise. The curves shown terminate<br />
at a 1 mm path-length difference, but data points corresponding<br />
to a 0.1 mm path difference are shown for<br />
all 3 frequencies. As can be seen, little further reduction<br />
in output noiae is achieved by decreasing the<br />
path-length difference from 1 to 0.1 mm. Thus, if the<br />
arms of the interferometer are matched to within 1 mm,<br />
phase shifts of 10-6 radians can be detected at 2 kHz.<br />
Attempts at reducing the path length difference to less<br />
than 1 mm would be futile. This is due to the fact that<br />
for an interferometer whose arms contain as much as a
100 meters of fiber, length changes on the order of 0.1<br />
mm can be expected as a result of changes in temperature,<br />
presaure, tension, and other environmental conditions.<br />
Thus, the fluctuation in laser optical output amplitude<br />
is eliminated. The subtraction is actually accomplished<br />
electrically in the differential amplifier following<br />
the photodetector as was shown in Fig. 4.7.<br />
Experimental verification of common mode rejection<br />
is shown in Fig. 4.18 (see Ref. 2 in Subsection<br />
6-<br />
a<br />
II<br />
~ 10.0 ~<br />
k<br />
OUTPUT FROM ONE PORT<br />
F<br />
m<br />
u<br />
(n<br />
u 1.0 -<br />
I<br />
L<br />
w<br />
d<br />
a<br />
01 -<br />
!3 OUTPUT OF BOTH PORTS<br />
u<br />
USING COMMON-MODE REJECTION /<br />
h<br />
a<br />
I<br />
I<br />
01 1 10 100 1000<br />
PATH LENGTH DIFFERENCE (mm)<br />
Fig. 4.17 Variation of homodyne interferometer output<br />
noise as a function of sensing arm path<br />
length difference for several output frequencies.<br />
After A. Dandridge, et al., Appl. Phys. Lett. ~, 77<br />
(1981)<br />
4.2.4 Amplitude Noise<br />
Common mode rejection refers to a method for<br />
the elimination of laser amplitude noise. Expressions<br />
for the optical intensity at the two output ports of<br />
the lower 3-dB coupler that was shown in Fig. 4.16 are:<br />
and<br />
11 = (1/2)(1 + ~sin~st) (4.19)<br />
12 = (1/2)(1 - ~sinust) (4.20)<br />
where I is the output optical intensity (power) of the<br />
laser minus the various insertion and fiber absorption<br />
losses. Aa is the amplitude of the phase shift produced<br />
by a signal of angular frequency us. Conservation<br />
of energy dictates the plus and minus signs in Eqs.<br />
(4.19) and (4.20) respectively. Summing Eqs. (4.19)<br />
and (4.20) yields I as required. Multiplying Eqs. (4.19)<br />
and (4.20) by 1 + AI/I where AI/I is an amplitude fluctuation<br />
whose ma nitude is the same order of magnitude<br />
as As, e.g. 10 -5 or 10-6, yields:<br />
and<br />
211 = I + AI + IAssinost (4.21)<br />
212 = I + AI - IAssin@st (4.22)<br />
where higher order terms in the infinitesimals AI/I and<br />
As are neglected. Subtracting Eq. (4.22) fromEq. (4.21)<br />
results in the expression:<br />
11 - 12 = IA a<br />
sinost (4.23)<br />
4-9<br />
Fig. 4.18 Minimum detectable phase shift versus fre -<br />
quency in a fiberoptic homodyne interferometric<br />
sensor using common-mode rejection<br />
of laser amplitude noise.<br />
After Dandridge and Tveten, Appl. Phys. Lett. ~, 2337<br />
(1981).<br />
4.2.8). The minimum detectable phase shift, expressed in<br />
microradians, is plotted versus frequency. The squares<br />
represent the output from a single port of the interferometer.<br />
The solid line is the average of these points.<br />
The circles are the data obtained when the output from<br />
both of the ports of the interferometer are detected<br />
and the different signals taken. By comparing these<br />
results it is seen that an order of magnitude decrease<br />
in the minimum detectable phase shift is achieved at<br />
low frequency. At frequencies above 1 kHz a minimum detectable<br />
phase shift of 0.1 urad (10-7 radians) is accomplished.<br />
This is representative of the kind of sensitivity<br />
that canbe achieved when common mode rejection<br />
is employed and the arms of the interferometer are<br />
matched to within 1 mm as was the case in this experiment.<br />
Laser noise due to satellite modes and multimode<br />
operation was also eliminated.<br />
4.2.5 Satellite Modea and Multimode Operation<br />
The influence of various amounts of optical<br />
feedback on the modal output of a Hitachic HLP 1400<br />
diode laser is shown by the output spectrum of the<br />
laser plotted for varioua conditions of optical feedback<br />
as shown in Fig. 4.19 (see Ref. 3 in Subsection<br />
4.2.8). Spectrum (a) is for the free running laser with<br />
a spectral width of 5 MHz. The spectra (b), (c), and<br />
(d) illustrate the effect of increasing amounts of feedback<br />
(from 0.04% to 1.5%). Notice that for spectra (b)<br />
and (c) the horizontal scale remains the same (i.e.,<br />
from -0.2 to +0.2 A) but for spectrum (d) the scale has<br />
changed, going from -6.0 to +6.0 A. The second and<br />
third curves correspond to 0.04% and 0.06% feedback.<br />
Here satellite modes appear and increaae as the amount<br />
of feedback increases. Such satellite modes arise as<br />
the result of coupling two resonant cavities: one the<br />
laser itself and the other the resonant cavity formed<br />
by the length of fiber from the laser to the primary<br />
reflection. Effects due to optical feedbacks of up to<br />
0.06% are eliminated when the interferometer lengths<br />
are matched to within lmm.
(a)<br />
&<br />
A<br />
FREE RUNNING<br />
Av = 5MHZ<br />
(c)<br />
(b)<br />
11<br />
I<br />
u<br />
0.2 0 0.2 0.2 0 0.2<br />
A<br />
A<br />
SATELLITE MODES<br />
Av = 0.02GHz Av= .12GHz<br />
0.04% 0.06%<br />
FEEDBACK FEEDBACK<br />
(<br />
606<br />
A<br />
MULTIMODES<br />
Av = 5GHZ<br />
1.5%<br />
FEEDBACK<br />
Fig. 4.19 Influence of optical feedback on the modal<br />
output of a Hitachi HLP 1400 diode laser.<br />
Adapted from R. Miles et al., Appl. Phys. Lett. ~,<br />
990 (1980).<br />
Spectrum (d) shows the effect of 1.5% feedback.<br />
Multimode laser operation results. In order to<br />
eliminate this effect, the back reflections into the<br />
laser must be maintained below approximately 0.06%.<br />
This is achievable with care. To accomplish this, it<br />
is necessary to assure that reflections from the end<br />
of the fiber are avoided. This requires the use of<br />
index-matching liquid between the laser and the fiber<br />
and furthermore the end of the fiber must be cut at a<br />
slight angle. All splices and couplers have to be<br />
carefully fabricated in order to reduce insertion loss.<br />
In the discussion of connections, it was shown that<br />
fiber misalignment would lead to insertion loss. These<br />
same misalignments will also lead to undesirable reflections.<br />
4.2.6 Phase-Locked Loop Operation<br />
The circuitry required to provide and insure<br />
quadrature operation in the presence of low frequency<br />
drift is shown schematically in Fig. 4.20 (see Ref. 4<br />
Fig. 4.20<br />
TWO STAGE INTEGRATOR,<br />
UNBIASED<br />
AMPLIFIER.<br />
PHOTODIODES<br />
CIRCUIT<br />
RESET<br />
KO<br />
M<br />
/)+“+ \<br />
/ I<br />
TO PZT PHASE SHIFTER<br />
J L 1<br />
-<br />
w /<br />
AMPLIFIER, HIGH PASS<br />
/<br />
..,FILTER. CUT OFFAT<br />
KD<br />
DIFFERENTIAL<br />
LOW FREQUENCY<br />
AMPLIFIER FOR<br />
LIMIT OF SIGNAL RANGE<br />
COMMON MODE<br />
REJECTION<br />
A phase-locked loop<br />
Cuit.<br />
t<br />
BANDPASS<br />
OUTPUT<br />
homodyne detection cirin<br />
Subsection 4.2.8). TWO photodiodea are shown on the<br />
left. The photodiodes are operated in an unbiased condition<br />
in order to eliminate dark current noise. Their<br />
outputs are combined in a differential amplifier that<br />
provides common-mode rejection as well as amplification.<br />
This is followed by two stages of integration<br />
that provide additional amplification. These two integrator-amplifiers<br />
pass all signals from DC up to the<br />
higheat frequency of interest. The output of the two<br />
stage integrator-amplifier is applied to a phase shifter<br />
located in the reference arm of. the interferometer.<br />
The phase shifter consists of either a lead zirconatelead<br />
titanate (PZT) cylinder around which the fiber in<br />
the reference arm is rather tightly wound or a section<br />
of polyvinylidene-floride (PVDF)-jacketed fiber. Both<br />
PZT and PVDF are piezoelectric materials. The output<br />
of the integrator-amplifier is just equal to the low<br />
frequency noise and the signal of interest. The effect<br />
then is to produce a phase ahift in the reference arm<br />
equal to that in the sensing anm, causing the interferometer<br />
to remain balanced, i.e., to phase-lock the system.<br />
If the phase were exactly locked there would be<br />
no output signal from the interferometer. However,<br />
there must be an error signal at the photodetectors in<br />
order to have a feedback signal. The amplification in<br />
the feedback circuit thus increaaes the error signal<br />
from the interferometer back up to the level of the<br />
signal being detected. If the system is initially at<br />
a bias (operating or quiescent) point away from quadrature<br />
there is insuffient output from the interferometer<br />
for the compensation circuit and the system till tend<br />
to drift toward an increasing error signal and therefore<br />
toward quadrature.<br />
The signal out of the compensating circuit is<br />
alao fed through a high-pass filter that has its low<br />
frequency limit set at the lowest frequency of interest.<br />
Therefore, the resulting output is a band of frequencies<br />
corresponding to the frequency range of interest.<br />
This constitutes the output of the interferometric sensor.<br />
Operational amplifiers (OPAMPS) are used in<br />
the feedback circuit and combined metal oxide semiconductor<br />
(CMOS) components in the reset circuit. The<br />
levels of voltage that can be applied by these circuits<br />
to the phase shifter are the order of + 10 volts. On<br />
the other hand, the range that the ph~se shifter can<br />
accommodate ia hundreds or thousands of volts. Furthermore,<br />
in many cases the amplitude of the phase drift<br />
resulting from temperatuze or pressure changes is much<br />
larger than the phase shift that would be generated by<br />
applying ~ 10 volts to the phase shifter. Thus, it is<br />
necesaary to keep track of how much voltage has been<br />
applied to the phase shifter and if the limit of the<br />
circuit begins to be reached it is necessary to rapidly<br />
reset the circuits back to the initial condition from<br />
which point it can start over. This is the purpose of<br />
the reset circuit indicated in Fig. 4.20. The phaae<br />
change associated with a large amplitude slow drift is<br />
compensated by a number of saw toothed-like amall amplitude<br />
phase changes. Care must be taken to minimize the<br />
noise introduced during the reset process.<br />
The upper frequency at which a measurement<br />
can be made is limited by the resonant frequency in the<br />
phase shifter itself. Phase-locked loop homodyne detection<br />
is particularly useful for frequencies below<br />
10 kHz. On the other hand, for casea where it is desired<br />
to make measurements at higher frequencies, say<br />
from a few kHz up to nearly a megahertz, heterodyne<br />
detection may be desirable.<br />
4.2.7 Heterodyne Detection<br />
Heterodyne detection is relatively insensi -<br />
tive to optical intensity fluctuations and low frequen-<br />
4-10
the aingle-sideband phaae noiae intercepts the 120 dB<br />
level at about 1 kHz. The acoustooptic modulator drive<br />
requirement is approximately +33 dBm. Asauming an output<br />
of +10 dBm from the oscillator the amplifier shown<br />
must provide 23 dBm of gain.<br />
Fig. 4.21<br />
cy noise. Phase trackers and the associated circuits<br />
are not required. An interferometer employing heterodyne<br />
detection is ahown in Fig. 4.21. The aystem difr<br />
UJO+<br />
SolMHz<br />
aLINEARFM<br />
DISCRIMINATOR<br />
‘A<br />
OU;PUT<br />
A interferornetric fiberoptic senaor employing<br />
heterodyne detection.<br />
fers from the usual heterodyne syatem in that uae is<br />
made of two Bragg cells. The firat cell also serves<br />
as a 3-dB coupler. By placing a star coupler (or plaited<br />
3-dB fiber coupler) at points A and B it should be<br />
possible for a single diode laser and one pair of Bragg<br />
cells to serve as the optical source for several dozen<br />
aenaors. For the Bragg frequencies indicated in Fig.<br />
4.21, bulk Bragg cells are required. In thia caae GRIN<br />
rods must be used to focus the light in and out of the<br />
fiber. If surface acoustic wave (SAW) Bragg cella are<br />
employed, they must be operated at approximately 600<br />
klllz (with a difference of 100 kHz). If the lowest signal<br />
frequency of interest is fs, the oscillator must<br />
exhibit phase noise less than -120 dB/Hz at an offset<br />
of fs from the carrier frequency. The plot of single<br />
sideband phase noise versus displacement from the carrier<br />
frequency for two oscillators is shown in Fig.<br />
4.22. The curve that corresponds to 600 MHz shows that<br />
5<br />
u -70<br />
u<br />
~ -80<br />
$1<br />
-90<br />
w<br />
~ -1oo<br />
z -110<br />
n<br />
z -120<br />
<<br />
flj -130<br />
Q<br />
m -140<br />
y -150<br />
60-100 MHz<br />
a ~ -160<br />
m<br />
I<br />
1 , ! !<br />
101 102<br />
,03 ,04<br />
105<br />
,.6<br />
FREQUENCY REMOVED FROM CARRIER<br />
Fig. 4.22 Typical single-sideband phaae noise measured<br />
relative to the carrier in a 1 Hz bandwidth<br />
in a fiberoptic interferornetric<br />
heterodyne sensor using fixed-frequency<br />
crystal osallators as shown in Fig. 4.12.<br />
4-11<br />
The maximum optical power that a channel waveguide<br />
will handle is about 120 uW. One pair of Bragg<br />
modulators configured as shown in Fig 4.21 could supply<br />
several sensors. However, with only 120 pW into the<br />
first Bragg cell it would not be possible to provide<br />
sufficient optical intensity to the detectors to insure<br />
quantum-limited operation for more than four sensors.<br />
Thua, for the operation of several dozen senaors from a<br />
aingle laser and one pair of bulk Bragg cells, heterodyne<br />
detection must be uaed.<br />
The difference frequency constitutes a heterodyne<br />
frequency of 100 kHz for the heterodyne detection<br />
configuration shown in Fig. 4.21. This permits the use<br />
of low-frequency, low-noise electronic circuits, such<br />
as low-noise amplifiers and FM discriminators. Since<br />
heterodyne detection is relatively insensitive to optical<br />
intensity fluctuation and low frequency noise,<br />
phase tracker circuits are not required. As in the<br />
case of homodyne detection, there may be a need for<br />
polarization-preserving fiber in order to prevent signal<br />
loss. Also, Bragg cells that are highly atable relative<br />
to each other, are required. Finally, in heterodyne<br />
detection, aa in homodyne detection, optical feedback<br />
into the diode laser greatly increases the laaer<br />
noise. Thus it is necessary to employ the aame precautions<br />
as were indicated above for homodyne detection.<br />
A number of other detection schemes have been<br />
suggested and are currently being considered. These<br />
include simple homodyning employing a 3 x 3 coupler in<br />
place of the input coupler (see Ref. 5 in Subsection<br />
4.2.8). It can be ahown that this resulta in an operating<br />
condition very close to quadrature. Synthetic<br />
heterodyne operation is another. A high frequency dither<br />
is employed on the phase stretcher. The output of<br />
such an interferometer can be shown to exhibit the characteristics<br />
of a heterodyne system.<br />
In view of the significant effort being applied<br />
to the detection problem further improvements can<br />
be expected; however, such effort la also an indication<br />
that the optimal detection acheme haa not been achieved.<br />
Numerous trade-offs are required. Theae include frequency<br />
range, sensitivity, dynamic range, cost, and complexity<br />
of the detection circuitry.<br />
4.2.8 References<br />
1.<br />
2.<br />
3.<br />
4.<br />
5.<br />
A. Dandridge, A. Tveten, R. Miles, D. Jackson, and<br />
T. Giallorenzi, “Single-Mode Diode Laser Phaae<br />
Noise”, Appl. Phya. Lett. — 38, 77 (1981).<br />
A. Dandridge and A. Tveten, “Noise Reduction in<br />
Fiber-Optic Interferometer Systems”, Appl. Opt.<br />
20-, 2337 (1981).<br />
R. Miles, A. Dandridge, A. Tveten, H. Taylor, and<br />
T. Giallorenzi, “Feedback-Induced Line Broadening<br />
in Cw Channel-Substrate Planar Laser Diodes”, Appl.<br />
Physica. Lett. — 37, 990 (1980).<br />
K. Fritsch and G. Adamovsky, “Simple Circuit for<br />
Feedback Stabilization of a Singlemode Optical<br />
Fiber Interferometer”, Rev. Sci. Instrum. ~, 996<br />
(1981).<br />
S. Sheem, “Fiber-Optic Gyroscope with [3x3] Directional<br />
Coupler”, Appl. Phys. Lett. 37, 869 (1980). —
4.3 INTEGRATED OPTICAL CIRCUITS (IOCS)<br />
The optical counterpart of the field of integrated<br />
electronics is the field of integrated optics.<br />
However, though integrated optical circuita have been<br />
made, they are for the moat part not commercially<br />
available. They are the subject of extensive research<br />
and development efforta at a large number of laboratories.<br />
The goal of these efforts is to commercially fabricate<br />
in large quantities these miniaturized devices<br />
with interconnected waveguides all on a single substrate.<br />
The generation, detection, propagation, modulation,<br />
switching, and coupling of light on such substrates<br />
have been accomplished. Techniques for the<br />
fabrication of substrates and the production of the<br />
high resolution material distribution patterns required<br />
for these integrated optical circuits exist. Most<br />
integrated optical circuits and associated devicea<br />
operate in a singlemode, therefore they are compatible<br />
with singlemode optical fibers. In essence most LEDs,<br />
diode lasers, and photodiodea are integrated optic<br />
devices. Integrated optical circuits are considered<br />
here because they are a part of second generation fiberoptic<br />
sensor technology.<br />
The waveguides used in integrated optical<br />
circuits are usually of two types namely planar films,<br />
that confine the light wavea in the vertical direction,<br />
and planar strips, (channels) that confine lightwaves<br />
in two dimensions. In both caaea, the waveguides are<br />
made of a higher refractive index than the surrounding<br />
material. Light is trapped in the layer or channel in<br />
much the same way that it is trapped in the core of an<br />
optical fiber. These planar waveguides can be formed<br />
by sputtering glass on a substrate of lower refractive<br />
index. A very uaeful type of channel waveguide can be<br />
formed by evaporating titanium (Ti) onto lithium niobate<br />
(LiNb03) or lithium tantalate in the desired<br />
waveguide patterns, and diffusing the Ti into the aubstrate<br />
thus forming a channel of higher refractive index.<br />
This is shown in Fig. 4.23. The attenuation in<br />
“’’”’””-r<br />
LiNb03<br />
SUBSTRATE<br />
“1<br />
OPTICAL<br />
n2<br />
CHANNEL&<br />
nl>nz<br />
Si02_<br />
ELECTRODES—<br />
Fig. 4.23<br />
n1>n2>n3<br />
(A) TITANIUM STRIP<br />
ON LiNb03<br />
SUBSTRATE<br />
(B) TITANIUM DIFFUSEDAT<br />
HIGH T INTO SUBSTRATE<br />
FORMING CHANNEL<br />
WAVEGUIDE<br />
(C) PROTECTIVE LAYEROF<br />
Si02 SPUTTERED<br />
ON SURFACE<br />
(D) ELECTRODES APPLIED<br />
Steps in the fabrication of a channel waveguide.<br />
auch channels is typically 1 dB/cm. A protective layer<br />
of silicon dioxide (Si02) ia often sputtered on top in<br />
order to protect the surface. Electrodes may be deposited<br />
on the Si02.<br />
Coupling a fiber to an integrated optic channel<br />
has been accomplished as shown in Fig. 4.24. The<br />
1 v “’SILICON<br />
SINGLE-MODE FIBEti<br />
IN ALIGNMENT<br />
V-GROOVES IN SILICON<br />
Fig. 4.24<br />
An optical fiber pigtailed to a lithium<br />
niobate (LiNb03) fiberoptic chip.<br />
fiber is aligned and epoxied in an etched silicon (Si)<br />
V-groove. The fiber end and the Si edge are polished<br />
and butted against the polished edge of LiNb03. Indexmatching<br />
liquid is used between the fiber and substrate<br />
ends. Similar techniques are uaed to couple diode<br />
lasers and photodetectors to the substrate. The dimensions<br />
of channel waveguides are close to those of both<br />
ainglemode fiber corea and the radiating areas of stripe<br />
geometry diode lasers. For stripe geometry, the long<br />
dimension of the channel should be oriented perpendicular<br />
to the long dimension of the radiating area of the<br />
diode. Insertion leases as low as a few dB can be<br />
achieved.<br />
Channel-to-channel couplers can be formed on<br />
the integrated optical circuit aubstrate by paralleling<br />
two channels in cloae proximity to each other for a<br />
sufficient distance to achieve the desired coupling<br />
ratio. The coupling length is defined as the distance<br />
required for complete power transfer to occur. The<br />
length required to achieve a apecified coupling ratio<br />
depends on the separation between channels and the refractive<br />
indices of the channels and subatrate. The<br />
refractive index of LiNb03 ia a linear function of the<br />
applied electric field. This is known aa the Pockels<br />
effect. Thus, if electrodes are applied as shown in<br />
Fig. 4.25, the refractive index can be varied and the<br />
light can be awitched to the other of the two output<br />
ports of the coupler. The direction of the electric<br />
field is oriented oppositely in the two channels resulting<br />
in equal and opposite refractive index changes.<br />
When the proper value of voltage is applied, the coupling<br />
length is made ahorter and the light will exit from<br />
the same fiber it entered. When the voltage is not applied,<br />
the coupling length is longer and the light will<br />
emerge from both ports. The exit channels from this<br />
switch may be combined to form the Mach-Zehnder interferometer<br />
shown in Fig. 4.26. The result is an electrooptic<br />
intensity modulator. When the light wavea recombine<br />
they excite the fundamental mode of the exit channel.<br />
When they arrive out of phase they tend to excite<br />
the aecond mode but the second mode can’t propagate in<br />
the singlemode channel, therefore it radiatea.<br />
An acoustooptic modulator (Bragg Cell) is<br />
ahown in Fig. 4.27. The interdigited ultrasonic transducer<br />
is shown at the bottom. The surface acoustic wave<br />
4-12
sets up periodic spatial fluctuations in the refractive<br />
index of the waveguide. These act as phase gratings<br />
deflecting a portion of the lightwave incident perpendicular<br />
to the resulting grating. The lightwave that<br />
passes straight through the grating exits with its frequency<br />
unchanged, while the diffracted ray has its frequency<br />
shifted by an amount equal to the acoustic frequency,<br />
e.g., 500 MHz. Such Bragg cells can be used<br />
for optical heterodyning.<br />
nl—An<br />
n, +dn<br />
+ l-l+<br />
ACOUSTIC ABSORBER<br />
I<br />
FREQUENCY<br />
SHIFTED BEAM<br />
ACOUSTIC<br />
SURFACE WAVE —–—=<br />
-—<br />
LIGHT<br />
.<br />
INCIDENT——<br />
UNDIFFRACTED<br />
/’ /<br />
BEAM<br />
OPTICAL FIBER<br />
/’<br />
INTERDIGITED<br />
CHANNEL / ‘ E3-- TRANSDUCER<br />
WAVEGUIDE<br />
ACOUSTIC ABSORBER<br />
ELECTRODES ( n.<br />
> LiNb03<br />
+h - , , /s.BsTRATE<br />
Fig. 4.27<br />
A Bragg cell integrated acoustic modulator<br />
in which an interdigital transducer is used<br />
for frequency shifting in accordance with<br />
an electrical input signal that develops an<br />
ultrasonic wave in a bifurcated optical<br />
waveguide.<br />
Fig. 4.25<br />
INCIDENT BEAMJ<br />
WAVEGUIDE<br />
A Pockels effect electrooptic binary switch<br />
mounted on a lithium miobate substrate.<br />
Technology exists for integrating an array of<br />
channel couplers connected to an array of photodiodes<br />
with charge-coupled device readout all on a single substrate.<br />
Using flip-chip techniques (mounting the chip<br />
face down) multiple fiber pigtails can be attached to<br />
a single chip. Such integrated devices promise to significantly<br />
reduce the size and cost of arrays of optical<br />
sensors.<br />
A<br />
MODULATED LIGHT OUT<br />
,-<br />
OP<br />
POLARIZ<br />
Fig. 4.26<br />
A Mach-Zehnder interferornetric electrooptic<br />
intensity modulator mounted on a lithium<br />
niobate (LiNb03) substrate chip.<br />
4-13
CHAPTER 5<br />
<strong>FIBEROPTIC</strong> <strong>SENSOR</strong>S AND COMPONENTS<br />
5.1 PHASE MODULATED <strong>FIBEROPTIC</strong> <strong>SENSOR</strong>S<br />
5.1.1 General<br />
A large variety of phase-modulated fiberoptic<br />
sensors have been demonstrated, including acoustic,<br />
electric, magnetic, rate of rotation, acceleration,<br />
electric current, trace vapor, pressure, and temperature<br />
sensors. They are being applied to hydrophores,<br />
magnetometers, gyroscopes, accelerometers, and other<br />
devices. These devices exhibit numerous advantages,<br />
the most important of which are geometric flexibility,<br />
immunity to electromagnetic interference (EMI) and<br />
electromagnetic pulses (EMP), large bandwidth, and<br />
great sensitivity i.e., ability to detect extremely low<br />
signal levels and small signal level changes. Phase<br />
shifts as small as 10-7 radians have been detected (See<br />
Ref. 1 in Subsection 5.1.7 at the end of this section).<br />
For a wavelength of 0.83 microns, this is equivalent to<br />
a length of approximately 10-14 meters, corresponding<br />
to the size of an atomic nucleus. Transduction, i.e.<br />
phase shifting, occurs as a lightwave travels throughout<br />
the sensing length of the optical fiber. Coherent<br />
light sources, singlemode fiber, and relatively complex<br />
optical and electronic circuitry are required.<br />
Consider<br />
shown in Fig. 5.1.<br />
LASER<br />
that have traveled independently through the two arms<br />
are recombined by a second 3-dB coupler that converts<br />
the phase-modulation to an intensity-modulation. The<br />
amplifiers and summing circuits combine the electrical<br />
signals from the photodiodes, one for each of the two<br />
output optical ports from the 3-dB coupler, in such a<br />
manner as to reject common mode noise, e.g., laser<br />
amplitude fluctuations. An integrator completes the<br />
phase-locked loop. The output signal is filtered to<br />
eliminate low frequency noise. In an alternate arrangement,<br />
both arms of the interferometer have a portion<br />
that is sensitive to the field being measured.<br />
These portions are spatially separated and therefore<br />
the combination is sensitive to the gradient of the<br />
field being measured. Using a homodyne detection<br />
scheme in a phase-locked loop configuration, phase<br />
shifts as small as 10-7 radians have been measured at<br />
frequencies above 1 kHz. The phase shifter in the reference<br />
arm is used as part of the phase-locked loop. The<br />
phase shifter can be fabricated by winding the fiber<br />
around a PZT stretcher or by applying a piezopolymer<br />
jacket on part of the fiber. In either case, the output<br />
of the amplifier/integrator circuit is applied to the<br />
phase shifter causing a phase modulation in the reference<br />
arm of the interferometer equal to that in the<br />
sensing arm. With this arrangement, the phase relation<br />
between the two arms of the interferometer is locked<br />
at the point of maximum sensitivity. This is known as<br />
quadrature operation.<br />
Various fiberoptic sensnr configurations are<br />
shown in Fig. 5.2. A planar arrangement is shown in<br />
Fig. 5.1<br />
the Mach-Zehnder interferometer<br />
Phase-locked loop homodyne detecm“:oDEs<br />
A phase-locked loop Mach-Zehnder-type homodyne-detection<br />
interferometer that cnnverts<br />
phase modulation to intensity (amplitude)<br />
modulation.<br />
tion, which is especially<br />
between 10 Hz and 20kHz, is<br />
mode fiber-ui~tailed diode<br />
suitable for frequencies<br />
shown. Light from a singlelaser<br />
is divided eaually<br />
between the” ~ms of the interferometer using a ‘solid<br />
state 3-dB fiber coupler. The sensing portion of the<br />
sensor arm is designed to respond to the field to be<br />
measured while the remainder of the sensing and reference<br />
arms are insensitive. The two beams of light<br />
Fig. 5.2<br />
SPATIAL SHADING<br />
aGRADlENT<br />
Optical fiber configurations used in fiberoptic<br />
sensors.<br />
the upper left. The linear array of spiral wound sensors<br />
in the lower left is suitable for beam forming.<br />
A spatially shaded element, such as in the upper right,<br />
where the spacings between windings vary according to<br />
a Gaussian distribution, possess a beam pattern exhibiting<br />
greatly reduced side lobes. Finally, the grad-<br />
5-1
ient configuration in the lower right is produced by<br />
utilizing both arms of the interferometer aa spatially<br />
separated sensors.<br />
5.1.2 Fiberoptic Acoustic Sensors<br />
5.1.2.1 Acoustic Pressure Sensors<br />
Extending the discussion for an acoustic sensor<br />
in Subsection 4.2.1 and considering Eqa. (4.7) and<br />
(4.8), the pressure variations associated with a sound<br />
wave produce phase fluctuations given by:<br />
A$ = kA(nL) = k(nAL + LAn) (5.1)<br />
is more nearly valid. Thus, the phase of a lightwave<br />
in Hytrelc-jacketed optical fiber, where the croas sectional<br />
area of the Hytrelc is much greater than that<br />
of the fused silica, responds to pressure according to<br />
the Hytrelc compressibility. While the results shown<br />
in Fig. 5.3 are for jacketed optical fibers, similar<br />
results are obtained when bare optical fiber is wound<br />
tightly on a Hytrelc or similar mandrel. In either<br />
case, the more compressible plastic (either jacket<br />
or mandrel), when subjected to fluctuating pressure,<br />
carries (atretches or compresses) the optical fiber<br />
along with it.<br />
A$ = kL(nAL/L + An) (5.2)<br />
where AL/L is the axial strain, S11; k is the wave num -<br />
ber; n is the refractive index of the core; and An is<br />
given by:<br />
An = -(n3/2)[(Pll + P12)S12 + P12S11] (5.3)<br />
where Pll and P12 are the Pockel’s coefficients and S12<br />
is the radial strain. A constant volume assumption<br />
yields the relation S12 = -S11/2. This assumption is<br />
valid only for a material whose Poisson’s ratio is close<br />
to 0.5. It is also quite good for the polyester jacket<br />
material Hytrelc, but not as good for fused silica.<br />
These materials exhibit values of Poisson’s ratio equal<br />
to 0.483 and 0.17 respectively. More exact treatments<br />
sre given in Refs. 2, 3, and 4 in Subsection 5.1.7.<br />
Substituting these relations into Eq. (5.3) yields:<br />
A$ = kLn[l+(n2/4)(Pll - p12)]Sll (5.4)<br />
In fused silica Pll = 0.12, P12 = 0.27 and n = 1.46.<br />
Substituting into Eq. (5.4) results in:<br />
A$ = 0.92kLnSll (5.5)<br />
For an isotropic material:<br />
AL/L = Av/3v :(1/3V)(~V/aP)AP (5.6)<br />
where AL/L = S11 is the axial strain, V iS the volume,<br />
P is the applied pressure and (1/V)(aV/ap) iS the com -<br />
pressibility, K. Thus:<br />
S1l = (1/3)KAP (5.7)<br />
With Kaa the wave number, Eq. (4.7) in Subjection 4.2.1<br />
reduces to $ = kLn. Using this and combining Eqs. (5.5)<br />
and (5.7) results in:<br />
A@/@AP = 0.307K (5.8)<br />
The compressibilities of silica and the pol~~<br />
ester Hytrelc are 2.7 x 10-11 and 2.67 x 10-10 pascals<br />
respectively, leading to:<br />
A$/$AP = 8.3 x 10-12 pascal-l<br />
for bare optical fiber and:<br />
A$/$AP = 8.2 x 10-11 pascal-l<br />
for Hytrelc jacketed optical fiber. Experimental values<br />
of A$/$AP, shown in Fig. 5.3, (See Ref. 5 in Subsection<br />
5.1.7) are 4.5 x 10-12 and 1.0 x 10-10 pascal-l respectively.<br />
The calculated and measured values agree to<br />
within 18% for Hytrelc and a factor of two for fused<br />
silica. These are quite reasonable agreements especially<br />
for Hytrelc where the constant volume assumption<br />
~lo -<br />
In<br />
PIJSTICCOAT(lmm)<br />
❑ DD<br />
❑ ODDDU ❑<br />
PLASTIC COAT (O.4 mm)<br />
00<br />
Ooooo(looooooooo(x o 0 0<br />
Q$<br />
SARE<br />
$<br />
<<br />
ALUMINUM COAT<br />
AAAAAAAAAAA A A 6 A A<br />
1 1 , 1 1 1 1<br />
0.2 0.4 O.b 0.8 10 12 1.4 16<br />
FREQUENCY (kHz)<br />
Fig. 5.3 Acoustic sensitivity vs frequency for various<br />
typea of optical fiber jacketing.<br />
Adapted from Lagakos et al., Opt. Soc. Am. ~, 460<br />
(1982).<br />
The discussion above is valid for the mandrelwound<br />
or thick-jacketed fibers. For thinner jackets,<br />
the phase sensitivity is a more complicated function<br />
of the elastic moduli. A low Poisson’s ratio will result<br />
in the thick-jacketed limit being approached with<br />
thinner jackets. Baaed on the criteria of large compressibility<br />
and low Poisson’s ratio, Teflon c appeara<br />
to be an optimum material. In order to demonstrate the<br />
effect of increasing jacket thickness. Ea. (5.2) is rewritten<br />
as:<br />
A$ = kLn(AL/L + An/n)<br />
= kLN[(l/L)aL/aP +<br />
and therefore, since $ = kLn as<br />
A$/$AP = (1/L)aL/aP +<br />
(1/n)an/aP]AP<br />
indicated above:<br />
(1/n)an/aP)<br />
‘CL,Z + Cn,z+cn,r<br />
J<br />
1<br />
(5.9)<br />
where CL z corresponds to the first term in the brackets<br />
and the 2n,z and cn,r correspond to the fiber axial and<br />
transverse components of the second term in the brackets.<br />
The last two terma are both associated with the<br />
pressure-dependence of the refractive index, n. The<br />
various values of the three components of A$/$AP are<br />
shown in Fig. 5.4 (see Ref. 4 in Subsection 5.1.7). As<br />
can be seen, the thick-jacketed fiber results were obtained<br />
for a jacket thickness of approximately 600Pm.<br />
5-2
-- ~ I<br />
I T I I I I<br />
1! 20 –<br />
~ c n.z<br />
9<br />
10<br />
‘0<br />
= ~ n,r<br />
0.0 ~— -–– –– ––––––––--–- - - - -<br />
%<br />
*<br />
g –10<br />
I<br />
value of A~$AP below that of fused silica, as was shown<br />
in Fig. 5.3. Theoretical results are shown in Fig. 5.6<br />
--<br />
1-a<br />
I T I r I I I I<br />
z –20<br />
><br />
~ –W<br />
%<br />
:<br />
y<br />
:<br />
0.5 –<br />
0.0 -<br />
%<br />
“ –40<br />
$<br />
~ -50 -<br />
< –so<br />
I I I I I I<br />
100 2(Y2 300 400 500 600<br />
HYTREL THICKNESS (pm)<br />
Fig. 5.4 The components of the per-unit phase change<br />
of a lightwave in a Hytrelc-jacketed fiber<br />
per pascal as a function of jacket thickness.<br />
After Lagakos and Bucaro, Appl. Opt. ~, 2717 (1981).<br />
In order to calculate the pressure sensitivity<br />
of one meter of Hytrelc-jacketed fiber, consider the<br />
experimental results that were given in Fig. 5.3. The<br />
measured value of A /@jAP, corresponding to a l-mm plastic<br />
jacket is 10-~0 pascal-l. Solving fOr A$/~ and<br />
taking L = 100 cm, n = 1.5, k = 7.4 x 104/cm (for A =<br />
0.85 microns) yields aA$/$of 10-6 radians for 10Q3<br />
pascals. Thus, 103 micropascals produces a one microradian<br />
phase shift. The pressure sensitivity per meter<br />
for this case is 60 dB re 1 micropascal. Increasing<br />
the length of optical fiber to 10 and 100 meters increases<br />
the pressure sensitivity to 40 dB re 1 micropascal<br />
and 20 dB re 1 micropascal respectively. These<br />
results are only 5 dB greater than the quantum limited<br />
theoretical results shown in Fig. 5.5. Included for<br />
3–0.5 —<br />
~<br />
: –10 -<br />
5~ –15 —<br />
CALCIUM ALUMINATE GuSS<br />
G<br />
z<br />
# –2.0 —<br />
g<br />
: –~,5 -<br />
$<br />
<<br />
0 20 40 60 SO 100 120 140<br />
COATING THICKNESS (pm)<br />
Fig. 5.6 Acoustic response (phase shift of a lightwave)<br />
in an optical fiber as a function of<br />
coating thickness.<br />
After Lagakos et al., Opt. Lett. ~, 460 (1982).<br />
(See Ref. 6 in Subsection 5.1.7) for jackets of nickel,<br />
calcium aluminate glass, and aluminum. A nickel jacket<br />
as thin as 10 microns should reduce the acoustic sensitivity<br />
of silica fiber to zero; however, the thickness<br />
is critical. On the other hand, a 90-micron jacket of<br />
aluminum is required for zero acoustic sensitivity but<br />
the thickness is much less critical. The variation of<br />
‘L,z~ ‘n,z~ cn,r, and A$/@P versus the thickness of<br />
the the aluminum jacket are shown in Fig. 5.7 (See Ref.<br />
5 in Subsection 5.1.7).<br />
4,<br />
--<br />
I<br />
2 -<br />
z<br />
:<br />
c1<br />
y<br />
0g<br />
%<br />
* –2 -<br />
~<br />
E n,z<br />
0 -––––––––––––-––-----–<br />
---——<br />
~ \ \<br />
— t \ H56EOUIV \<br />
d<br />
~ 30 cOATEDFIBE’R 115fiW20ml<br />
Y\Y<br />
+<br />
I<br />
3 5 10 2 5 100 2 5 1,000 2 5 Io,orm<br />
FREQUENCY (H,]<br />
Fig. 5.5<br />
Variation of acoustic energy spectrum level<br />
as a function of frequency for two coated<br />
fibers along with other noise levels in a<br />
sea subsurface environment.<br />
comparison in Fig. 5.5, are various ambient noises,<br />
such as shipping, weather and seismic noiaes. Also<br />
shown is the equivalent noise pressure of the U.S.<br />
Navy’s H56 hydrophore.<br />
o 20 40 60 80 100 120 140<br />
ALUMINUM THICKNESS (pm)<br />
Fig. 5.7 Pressure components per unit sensitivity<br />
per unit pressure as a function of aluminum<br />
jacket thickness on an optical fiber.<br />
After Lagakoa and Bucaro, Appl. Opt. — 20, 2719 (1981).<br />
5.1.2.2<br />
Pressure Gradient Sensors<br />
The effect of jacketing optical fiber with<br />
aluminum (measured experimentally) is to reduce the<br />
mined by<br />
The direction of a sound source can be deterusing<br />
either an array of omnidirectional sen-<br />
5-3
sors or a pressure gradient sensor. Sensor arrays will<br />
be considered in Chapter 6. Pressure gradient hydrophores<br />
sense the pressure at two closely spaced points.<br />
The distance between sensors, S, iS typically much less<br />
than the wavelength of sound, k, in the propagation<br />
medium, namely water in the calculations that follow.<br />
A pressure gradient measurement can be accomplished by<br />
means of either two distinct sensors, one at each point,<br />
or by a single senaor apanning the distance between the<br />
two points. Both types of sensora will be considered<br />
here.<br />
Since the output signal from a pressure-gradient<br />
hydrophore is proportional to the preasure gradient,<br />
ita reaponse ia proportional to the particle velocity.<br />
Such sensors are therefore often called particle<br />
velocity hydrophores. This is an advantage when operating<br />
near a pressure releaae aurface where the particle<br />
velocity almost doublea and the pressure itself goes to<br />
zero. The tendency to reapond to particle velocity<br />
renders them more aensitive to flow noiae than omnidirectional<br />
hydrophores. Thia follows because particle<br />
velocity fluctuations associated with flow are often<br />
much greater than the particle velocity oscillations<br />
associated with the acoustic signal being measured.<br />
Consider the sine wave shown in Fig. 5.8 where the<br />
Fig. 5.9<br />
100<br />
90<br />
80<br />
70<br />
60<br />
50<br />
40<br />
30<br />
20<br />
\<br />
1<br />
3 5 ID 2 5 100 2 5 1,000 2 5 10,000<br />
FREOUENCY (Hz)<br />
HEAVY<br />
SS2 WIND<br />
SPEED<br />
10 KTS<br />
RAIN<br />
V a r i a t i o n of the acouatic energy spectrum<br />
level aa a function of frequency for a fiberoptic<br />
presaure-gradient hydrophore with<br />
other noise levels in a sea subsurface environment.<br />
P<br />
PA- -<br />
I<br />
The calculated reaults shown in Fig. 5.9 is<br />
for the case of the aound wave propagating parallel to<br />
the line joining the two sensors. The sensitivity of<br />
a Preasure gradient sensor to a sound wave propagating<br />
perpendicular to this direction ia zero because both<br />
sensors are then aubjected to the aame pressure. The<br />
directivity is dipole-like aa shown in Fig. 5.10(a).<br />
The cardioid directional responae shown in Fig. 5.10(b)<br />
can be obtained by combining the dipole output with<br />
that of an omnidirectional hydrophore with sensitivity<br />
equal to that exhibited by the dipole at e = OO. The<br />
Fig. 5.8<br />
The pressure distribution aa a function of<br />
distance from the zero-preasure point of a<br />
single pressure wave.<br />
instantaneous acoustic preasure, P, is given by:<br />
p = pAsiI’i (2~/ka)x (5.10)<br />
where pA is the acoustic amplitude, as is the sound<br />
wavelength, and x is distance in the same units as ~.<br />
The pressure amplitude at x = O and x = S (S
Since neutral bouyancy is required, m/AS = maaa per unit<br />
volume = 1 and Eq. (5.13) becomes:<br />
tin = (2T/k~)pA (5.14)<br />
Thus, once the sound frequency (wavelength, 1s) and<br />
pressure level are chosen, the acceleration can be<br />
determined. For f = 100 Hz (As = 1460 cm) and PA = 50<br />
dB re 1 micropascal, corresponding to the 118-met r<br />
curve that waa shown in Fig.<br />
= 1.67 -3<br />
X 10 g<br />
(1.6 gal). This requires an5;1;r~%Ny sensitive accelerometer.<br />
The two-fiber accelerometer described<br />
below exhibits the required sensitivity.<br />
5.1.3 Fiberoptic Magnetic Sensors<br />
Yariv and Winsor (See Ref. 7) suggested that<br />
an optical fiber could be used to measure the change<br />
in length of a magnetostrictive material subjected to<br />
a magnetic field. The resulting optical phase change<br />
is linearly related to the magnetic field. Jarzynski,<br />
et.al. (See Ref. 8 in Subsection 5.1.7) developed expressions<br />
for the strain induced in a magnetostrictively-jacketed<br />
fiber subjected to a weak axial magnetic<br />
field. These expressions were obtained as a function<br />
of jacket thickness for a variety of magnetostrictive<br />
materials as shown in Fig. 5.11. The magnetooptic<br />
J<br />
10 100 1,000 10,000<br />
FREQUENCY (HZ)<br />
Fig. 5.12 The magnetooptic coupling coefficient versus<br />
frequency for an optical fiberwound<br />
nickel toroid with walls 0.038 cm thick.<br />
After J. Cole et al., Opt. Lett. ~, 216 (1981).<br />
\ /-WINDING<br />
.<br />
10.0<br />
t<br />
4.5% CO.95.5% Ni<br />
-TOROIDAL<br />
WINDING<br />
8.0 -<br />
70<br />
-1<br />
*j<br />
aXO<br />
6.0 -<br />
4.0 -<br />
2.0 -<br />
2V-PERMENDUR<br />
HOUSING<br />
Fig. 5.13 Optical fiber wound on a magnetostrictive<br />
nickel toroid (wall thickneas 0.038 cm) for<br />
use in meaauring the magnetooptic coupling<br />
coefficient.<br />
After J. Cole et al., Opt. Lett. ~, 216 (1981).<br />
I , , # 1 # 1 , 1<br />
0 5 IO 15 20 25 30 35 40<br />
METAL JACKET THICKNESS (pm)<br />
Fig. 5.11 Magnetic sensitivity of magnetostrictive<br />
metal-jacketed optical fiber as a function<br />
of jacket thickness for various magnetostrictive<br />
metals.<br />
Adapted from J. Jarzynski et al., Appl. Opt. ~, 3746<br />
(1980).<br />
coupling coefficient as shown in Fig. 5.12 was measured<br />
for nickel by Cole, et.al. (See Ref. 9 in Subsection<br />
5.1.7) using a nickel cylinder around which the optical<br />
fiber in one arm of the interferometer was wound as<br />
shown in Fig. 5.13). The relevant theory has been compared<br />
with magnetooptical experimental data taken at<br />
low frequency (< 1 kHz) and msgnetomechanical data<br />
taken at frequencies greater than several tens of kilohertz.<br />
Thia study demonstrated that the piezomagnetic<br />
atrain coefficient remains constant from low frequency<br />
up to the frequency at which eddy currents become important.<br />
Therefore, the low frequency measurement reaults<br />
may be uaed to design magnetic sensors that will<br />
operate at high frequencies, i.e., to the eddy current<br />
limit.<br />
Magnetoatrictive materials have been used extensively<br />
as acoustic transducers for the production or<br />
detection of sound. In the preaent application these<br />
materiala are used to detect magnetic fields by measuring<br />
the reaulting atrain produced. The most atraight<br />
forward and sensitive technique for such measurements<br />
involvea uaing an optical fiber in one arm of a Mach-<br />
Zehnder interferometer. The fiber is either jacketed<br />
with the magnetostrictive material or wound around a<br />
magnetostrictive mandrel. The resulting change in optical<br />
path is due to changes in both the refractive<br />
index and the length of the optical fiber core. This<br />
leads to a phase ahift A+ given by Eq. (5.5) in Subsection<br />
5.1.2.1. An expression for S11 can be obtained<br />
from the effective piezomagnetic strain constant dT defined<br />
by the expression:<br />
dT = 4n(3S11/aH)T (5.15)<br />
where T is the streaa.<br />
yields:<br />
Integrating this expression<br />
Sll = (1/41r) a ‘b dTdH (5.16)<br />
where the limits a and b are Ho-Hi/2 and Ho+H1/2, respectively,<br />
H. is the dc bias field choaen to ~ximize<br />
dT, and HI is a small excursion about that point. For<br />
5-5
nickel H. = 3.6 oersteds and for a small excursi n<br />
about the maximum, dT r~~ains constant at 8 x 10 -8 .<br />
Therefore, S1l = 6.4 x 10 HI and:<br />
Using this technique a<br />
1o-8 A/m waa measured<br />
to 5000 Hz.<br />
minimum electric current<br />
over the frequency range<br />
of 3 x<br />
100 Hz<br />
@/kLHl = 8.6 X 10 -7 oersteda -1 (5.17)<br />
is the magnetooptic coupling coefficient. This agreea<br />
quite well with the value of coupling coefficient between<br />
7 and 8 x 10-7 measured by Cole et.al. (See Fig.<br />
5.12 and Ref. 9 in Subsection 5.1.7). The value of dT<br />
used in Eq. (5.16) was measured at approximately 30 kHz<br />
and has been shown to be valid up to the frequency at<br />
which eddy current limitations occur.<br />
Using the measured magnetooptic coupling coefficient<br />
shown in Fig. 5.12, the minimum detectable<br />
magnetic field (oersteds) per meter of nickel-jacketed<br />
optical fiber can be calculated. From Fig. 5.12, for<br />
A$ = 7.5 x 10I7 kLH, and using k = 7.4 x 10-4 (for 0.85<br />
micron optical radiation), L = 102 cm, and 10-6 radians<br />
minimum detectable phase shift, the minimum detectable<br />
magnetic field for 1 meter of nickel-jacketed optical<br />
fiber is 1.8 x 10-7 oersteds (1.8 x 10-2 gamma). Recently<br />
a minimum detectable magnetic field of 5 x 10-9<br />
oersted per meter of fiber waa measured using optical<br />
fiber jacketed with an amorphous magnetostrlctlve material<br />
(See Ref. 10). Extrapolating to 1 km of such metallic<br />
glass-jacketed fiber leads to the prediction<br />
that magnetic fields as amall as 5 x 10-12 oersteds may<br />
be detected by this means. On the other hand a one cm<br />
length of such jacketed fiber should permit the measurement<br />
of a magnetic field as small as 5 x 10-7 oersted<br />
(0.05 gamma).<br />
The sensitivities of pressure, magnetic, and<br />
temperature fiberoptic sensors is summarized in Fig.<br />
5.14. The cross section configuration of the various<br />
jacketed optical fiber is shown in the middle column.<br />
The predicted sensitivities corresponding to one mlcroradian<br />
phase shift for one meter of jacketed fiber is<br />
shown in the last column.<br />
FIBER<br />
a<br />
FIBER<br />
I<br />
ALUMINUM<br />
TUBING<br />
\“<br />
Fig. 5.15 Fiberoptic senaors for measuring electrical<br />
currents.<br />
After A. Dandridge et al., Electron. Lett. ~, 524<br />
(1981).<br />
The second technique, also shown in Fig. 5.15,<br />
depends on the resistive heating that occurs in a section<br />
of aluminum jacketed optical fiber as a result of<br />
passing the electric current to be measured through the<br />
jacket. Using this technique aminimum detectable electric<br />
current of 1.3 x 10-5 A/m was measured at 1 Hz.<br />
5.1.5 Fiberoptic Spectrophones<br />
Spectrophones are used to determine the preaence<br />
of trace vapors by means of the acoustic signal<br />
produced by the temperature increase associated with<br />
the absorption by the vapor of a pulsed laser output.<br />
Conventional microphones are used to detect the acoustic<br />
signal. The schematic of a fiberoptic spectrophone<br />
(See Ref. 12 in Subsection 5.1.7) is shown in Fig. 5.16.<br />
<strong>SENSOR</strong> TYPES<br />
CONFIGURATIONS<br />
FI?EDICTED PERFORMANCES<br />
A~-W-6RAD, lMETER FISER)<br />
op,Geo~<br />
339u”ItleNe<br />
LASER<br />
PRESSURE<br />
Si02<br />
P~NX 60dS re #Pa<br />
LASTOMER<br />
MAGNETIC<br />
aSiO*,0e02<br />
SiO*<br />
MAGNETO–<br />
STRICTIVE<br />
HMNZ 5xlo”90ERsTED<br />
(METALLIC GLASS)<br />
06328 ”. H?Ne<br />
LAsER@<br />
TEMPERATURE<br />
SiO~<br />
Si02, GeO~<br />
e METAL<br />
ATMNZ FTSC”<br />
Fig. 5.14 Fiberoptic sensor performance parameters<br />
(coefficients) for several fiber jackets.<br />
5.1.4 Fiberoptic Electric Current Sensors<br />
Two techniques for measuring electric currents<br />
are shown in Fig. 5.15 (See Ref. 11 in Subjection<br />
5.1.7). In the first, a section of nickel-jacketed<br />
fiber is located in the center of a solenoid energized<br />
by the current being meaaured. By measuring the magne -<br />
tic field intensity, the electric current is determined.<br />
Fig. 5.16 A fiberoptic spectrophone for detecting the<br />
pressence of trace vapors.<br />
After D. Leslie et al., Electron. Lett. ~, 581 (1981).<br />
The frequency of the excitation laser is equal to an<br />
excitation frequency in the absorption spectrum of the<br />
trace vapor being detected. The absorption cell consists<br />
of a thin walled cylinder around which is wound<br />
a fiberoptic coil to form one arm of a Mach-Zehnder<br />
interferometer. The fiber coil serves as the microphone.<br />
It has the advantage of not requiring electri-<br />
5-6
cal leads in the vicinity of the vapor. The chopper<br />
is operated at a frequency at which the acoustic aenaitivity<br />
of the absorportion cell is high.<br />
The light from the excitation laser excites<br />
a characteristic absorption line in the molecular spectrum<br />
of the vapor being detected. When the excited<br />
molecules return to equilibrium the temperature of the<br />
vapor Is increased resulting in a preaaure increase.<br />
By chopping (interrupting) the light at a given rate<br />
(frequency), the resultant fluctuation in preasure Is<br />
detected as aound of the same frequency. Even more<br />
desirable 1S to make use of a variable frequency laaer<br />
aa the excitation source. The absorption coefficients<br />
vs. frequency of ambient atmosphere and of methane<br />
whose concentration 1S five times ambient are shown in<br />
Figs. 5.17 and 5.18.<br />
measure strains, electric fields, temperature, acceleration,<br />
and rate of rotation. They differ from the<br />
acoustic and magnetic senaors discussed above that rely<br />
on specialized jacketa and utilize a Mach-Zehnder interferometer.<br />
The electric current and trace vapor sensors<br />
are secondary devices relying on the measurement<br />
of the magnetic field or the temperature in the former<br />
case and the aound associated with the absorption of<br />
light in the latter case.<br />
5.1.7 References<br />
1.<br />
2.<br />
3.<br />
D. Jackson, A. Dandridge, and S. Sheem, Opt. Lett.<br />
~, 139 (1980).<br />
B. Budiansky, D. Drucker, G. Rino, and J. Rice,<br />
APP1. Opt. ~, 4085 (1979).<br />
G. Hocker, Opt. Soc. Am. ~, 320 (1979).<br />
lo”~<br />
WAVELENGTH<br />
Fig. 5.17 The absorption coefficient of ambient atmosphere<br />
aa a function of wavelength.<br />
Provide by D. Leslie, U.S. Naval Reaearch Laboratory.<br />
4.<br />
5.<br />
6.<br />
7.<br />
8.<br />
9.<br />
10.<br />
11.<br />
N. Lagakos and J. Bucaro, Appl. Opt. — 20, 2716<br />
(1981).<br />
N. Lagakos, T. Hickman, J. Cole and J. Bucaro,<br />
Opt. Lett. ~, 443 (1981).<br />
N. Lagakos, private communication.<br />
A. Yariv and H. Winsor, Opt. Lett. ~, 87 (1980).<br />
J. Jarzynski, J. Cole, J. Bucaro and C. Davia,<br />
Appl. Opt. ~, 3746 (1980).<br />
J. Cole, N. Lagakos, J. Jarzynski, and J. Bucaro,<br />
Opt. Lett. ~, 216 (1981).<br />
K. Koo and G. Sigel, Technical Digest, Optical Fiber<br />
Communication Meeting, Phoenix, Arizona (1982)<br />
p. 72.<br />
A. Dandridge, A. Tveten, and T. Giallorenzi, Electron.<br />
Lett. ~, 523 (1981).<br />
ABSORBERS<br />
TYPE (TORR)<br />
H20 14.260<br />
C02 0,251<br />
03 2.3x lC”5<br />
~’”i<br />
N20 2.1 X1 O-4<br />
co 5.7 x10-5 I<br />
CH4 12’1 0-31 1II I<br />
159627<br />
02<br />
1~ II<br />
WAVELENGTH<br />
22.9°C<br />
JJ<br />
760 TORR<br />
Fig. 5.18 The absorption coefficient of methane gas<br />
as a function of wavelength for a concentration<br />
of 7.6 x 10-3 torr (5 x ambient).<br />
Provide by D. Leslie, U.S. Naval Research Laboratory.<br />
12.<br />
5.2<br />
D. Lealie, G. Trusty, A. Dandridge and T. Giallorenzi,<br />
Electron. Lett. ~, 581 (1981).<br />
5.2.1 General<br />
INTENSITY MODULATED <strong>FIBEROPTIC</strong> <strong>SENSOR</strong>S<br />
The second type of fiberoptic sensor to be<br />
diacusaed is referred to as an intensity-modulated aensor.<br />
Ita basic configuration is sketched in block diagram<br />
form in Fig. 5-19. The output lightwave from an<br />
OPTICAL<br />
SOURCE<br />
+ l~”T<br />
<strong>SENSOR</strong><br />
OPTICAL<br />
DETECTOR<br />
.<br />
‘OUT<br />
5.1.6 Summary<br />
The acoustic and magnetic field sensors described<br />
above represent primary measurement devices.<br />
Other primary measurement devices include sensors to<br />
TIME<br />
TIME<br />
TIME<br />
Fig. 5.19 A generalized intensity-type fiberoptic<br />
senaing system.<br />
5-7
optical source of constant intensity IIN (shown at the<br />
lower left) is injected into the sensing element. This<br />
element, acted on by an external force field (baseband<br />
signal), represented in the figure as an incident ainusoidally-varying<br />
quantity, alters the intensity of the<br />
light transmitted through the sensor. The modulation<br />
envelope of the output intensity, IOUT, matches that of<br />
the input force field (signal). In turn, the time varying<br />
output optical intensity, incident on the photodetector,<br />
similarly modulates the output voltage, eo~.<br />
The intensity-modulation sensor shown in Fig.<br />
5.19 employs relatively simple optica and circuitry. An<br />
incoherent optical source, such as an LED, or a highintensity<br />
incandescent source, may be used, together<br />
with multimode fibers as links between the sensing element<br />
and the source and detector. The sensor itaelf<br />
typically consists of one or two multimode fibers or<br />
some mechanooptic, electrooptic or other atraight forward<br />
transduction element. Achievable sensitivities,<br />
expresaed in terms of minimum detectable displacements<br />
for intensity-type mechanical motion detectors, lie in<br />
the ran e 10-10 to 10-7 m, as compared to a lower limit<br />
of 10-1 fm achievable with interferometric type fiberoptic<br />
sensors.<br />
5.2.2 Evanescent-Field Fiberoptic Sensor<br />
To illustrate the various types of intenaity<br />
modulation transduction mechanisms currently under investigation,<br />
consider first the evanescent field transducer<br />
(see Ref. 1 in Subsection 5.2.6) outlined in Fig.<br />
5.20. It consists of a pair of single or multimode op-<br />
L .<br />
:;cm;<br />
OPTICAL<br />
DETECTOR<br />
I<br />
CORE<br />
CLADDING ‘2<br />
CLADDING<br />
FIBER<br />
<strong>SENSOR</strong><br />
\’<br />
—MIRRORED<br />
Fig. 5.21 A critical-angle intensity-type fiberoptic<br />
sensor.<br />
After R. Phillips, Opt. Lett. ~, 318 (1980).<br />
in the optical reflection coefficient (See Ref. 2 in<br />
Subsection 5.2.6) at the right hand tip of the fiber.<br />
Referring to the upper portion of Fig. 5.21, light injected<br />
into the core at the left end of the fiber is<br />
partially reflected back along the length of the fiber<br />
and then directed to the photodetector using a beam<br />
splitter. As indicated in the lower expanded view of<br />
the right end of the fiber, two reflecting facets are<br />
lapped on the end of the fiber. The lower facet is<br />
coated so that it ia totally reflecting. By carefully<br />
controlling the angle of the upper facet so that the<br />
beam in the core is incident at an angle larger than<br />
the critical angle, the light in the core will be partially<br />
transmitted into the medium of refractive index<br />
n3 in contact with the end of the core. Slight variations<br />
in n3, induced by changea of pressure or temperature,<br />
for example, will change the intensity of the<br />
reflected beam. One can thus envisage a probe or catheter-type<br />
presaure transducer, of active area equal to<br />
that of the end of the core, i.e., effectively a point<br />
pressure probe, that could be superior in many ways to<br />
some of the more conventional types that are in use<br />
today.<br />
d -CORE SPACING<br />
L- INTERACTION LENGTH<br />
OPTICAL<br />
DETECTOR<br />
5.2.4 Moving Grating Fiberoptic Sensor<br />
A conceptually simple intensity-type aensor<br />
is the moving grating transducer shown in Fig. 5.22<br />
(See Ref. 3 in Subjection 5.2.6). Two fibers are sep-<br />
Fig. 5.20 .An evanescent-field intensity-type fiberoptic<br />
sensor.<br />
MOVABLE<br />
GRATING<br />
STATIONARY<br />
~GRATING<br />
tical fibers. In the transduction element itself the<br />
cladding is reduced In thickness, or entirely removed,<br />
so that the distance, d, between the cores is small<br />
enough to permit evanescent field coupling between the<br />
two fibers over some small interaction length L. Coupling<br />
may be enhanced by potting the interaction response<br />
in a fluid or flexible elastomer of refractive index,<br />
nz, the same as that of the cladding. Slight variations<br />
of the spacing, d, the interaction length, L, or<br />
the refractive index, n2, induced by the particular<br />
force field of interest may produce substantial changes<br />
of the light coupled into the lower or pick-up fiber.<br />
Promising results have been reported on two hydrophonetype<br />
applications of this modulation mechanism. Further<br />
studies are in progress.<br />
Fig. 5.22<br />
H<br />
A moving-grating<br />
senaor.<br />
1<br />
I<br />
CORE<br />
TO<br />
DETECTOR—<br />
I<br />
1nCLADDING<br />
intensity-type fiberoptic<br />
5.2.3<br />
shown in<br />
Reflection Coefficient Fiberoptic Sensor<br />
A second intensity-type fiberoptic sensor is<br />
Fig. 5.21. Its operation is based on changea<br />
5-8
arated by a small gap in which is placed a pair of gratings,<br />
consisting of a cyclic grid of totally transmissive<br />
and totally reflecting (opaque) parallel line elements<br />
of equal width. When the gratings are moved relative<br />
to one another there is a change In the transmitted<br />
intensity. This type of transducer has been employed<br />
in a hydrophore, as sketched in Fig. 5.23. Here one<br />
DIAPHRAGM<br />
n \ n<br />
L<br />
r<br />
HYDROPHORE<br />
/HOUSING<br />
/<br />
be seen that the sensitivity will be greatest when the<br />
quiescent or bias point is set at a relative displacement<br />
of 2.5 pm, 7.5 pm, 12.5 pm, etc. In addition, decreasing<br />
the width of the grating elements will increase<br />
the sensitivity but decrease the dynamic range.<br />
5.2.5 Microbend Fiberoptic Sensor<br />
The intensity-type sensors to be considered<br />
last are based on microbend-induced ejection of light<br />
from the core of a fiber into the cladding (See Ref. 4<br />
in Subsection 5.2.6). Referring to Fig. 5.25, the<br />
transduction element in this type of sensor consists<br />
of a deforming device such as a pair of toothed or serated<br />
plates that introduce small bends in a fiber. As<br />
FIBER<br />
\<br />
I<br />
F<br />
I<br />
DEFORMER<br />
F<br />
I<br />
I , I<br />
OPPOSED GRATING<br />
Fig. 5.23 A moving grating intensity-type fiberoptic<br />
sensor used in a hydrophore.<br />
Adapted from W. Spillman, Appl. Opt. ~, 465 (1981).<br />
of the gratings is shown mounted on the rigid base<br />
plate of the housing while the other is attached to a<br />
flexible diaphragm. The diverging lightbeam from the<br />
input fiber on the left is collimated using a short<br />
graded-index self-focusing (Selfocc) lens and then partially<br />
transmitted through the gratings as a parallel<br />
(collimated) beam that is focused into the output fiber<br />
using a second self-focuaing (Selfocc) lens. Assuming<br />
the two gratings each consist of 5 pm-wide grating elements<br />
that are spaced 5 Bm apart, the transmitted light<br />
intensity will vary cyclically as sketched in Fig. 5.24,<br />
passing through successive maxima each time the grating<br />
displacement changes by 10 ~m. From this graph it may<br />
1.0<br />
MODE1:<br />
E1-sin(LJt-~lz)<br />
MODE2: E2-sin(Ut–~2z)<br />
COUPLING CONDITION: L=— 13;:132<br />
Fig. 5.25 A microbend intensity-type<br />
ser.<br />
fiberoptic senahowo<br />
in the figure, the distance L between adjacent<br />
teeth defines the apatial frequency of the deformer. By<br />
increasing the force, F, applied to the plates the amplitude<br />
of the deformations can be increased. In the<br />
earlier brief discussion of attenuation mechanisms in<br />
fibera, it was shown that random bends in fibers can<br />
cause light to be ejected from the core into the cladding.<br />
Thia process is illustrated in the enlargement<br />
of the deformer shown in Fig. 5.26. Rays propagating<br />
~
in a straight section of the fiber at an angle less<br />
than the critical angle may have their angle of incidence<br />
on the core-cladding interface increased by the<br />
bends and thus be partially transmitted into the cladding.<br />
A more detailed wave theory analysis of periodic<br />
bend-induced coupling indicates that the level of coupling<br />
between modes, including non-attenuating core modes<br />
as well as attenuating core and cladding modes, is<br />
strongest when the difference between the effective<br />
propagation constants of a pair of modes, (Bi - Bj), is<br />
equal to 2 /1..<br />
range 0.5N < F > 1.5 N. In the latter caae, 9“ corresponded<br />
closely to the critical incidence angle, thus<br />
the light waa injected mainly into the highest order<br />
propagating modes and therefore was more eaaily ejected<br />
from the core into the cladding.<br />
loofiT_..-<br />
,_L<br />
1::::-,-<br />
1 I 1 I I I I I I I I I I<br />
T – - * — - 0 - - 1<br />
A number of studies of this phenomenon have<br />
been conducted. For example, the system shown in Fig.<br />
5.27 was used at the Hughes Research Laboratories. As<br />
EO<br />
~ —<br />
L<br />
I<br />
FIBER<br />
DETECTOR MODE DEFORMER<br />
STRIPPER<br />
Fig. 5.27 A microbend intensity-type<br />
sor system developed by the<br />
Laboratories.<br />
fiberoptic sen-<br />
Hughes Research<br />
indicated in the figure, light was injected into a<br />
multimode step-index fiber which was passed through a<br />
deformer element. In this case the intensity of the<br />
core light reaching the end of the fiber was monitored.<br />
By using a helium-neon laser with a well-collimated<br />
beam it was possible to vary the incidence angle of<br />
light into the fiber and thus inject light into a fairly<br />
well defined set of propagating core modes. On sections<br />
of the cladding, just before and just after the<br />
deformer, mode strippers were employed. These elements,<br />
which in their simplest form might consist of black<br />
paint applied to a few centimeters of the outer surface<br />
of the cladding, absorb almost all of the light that<br />
my be propagating in the cladding of the fiber. The<br />
use of cladding mode strippers first insured that only<br />
core light reached the section of fiber in the deformer<br />
and then that any core light ejected into the cladding<br />
by the deformer was absorbed so that it did not reach<br />
the photodetector.<br />
Uaing the system outlined in Fig. 5.27, the<br />
Hughes’ inveatigatora measured the transmitted optical<br />
intensity as a function of the force applied to the<br />
transducer (microbend deformer). This was done for<br />
several different angles of incidence of the input light<br />
and the reaulting data la preaented in Fig. 5.28. Aa<br />
shown in that figure, when the input incidence angle<br />
was set at 0°, i.e., for light injected along the axis<br />
of the fiber, the output intensity decreased by about<br />
twenty percent as the force applied to the deformer increaaed<br />
from O to 2 newtons. On the other hand, for<br />
light incident at 9°, the transmitted intensity decreased<br />
to approximately 40 percent of the input when the<br />
applied force waa again increased to 2 N. In addition,<br />
the slope of the transmission intensity, I, veraus applied<br />
force, F, curve was nearly conatant over the<br />
1<br />
r<br />
r<br />
——— O.ODEG .<br />
20<br />
----- 7.ODEG 0<br />
-“---”- 8.ODEG ❑ 1<br />
} ------- 9.0 DEG ●<br />
4<br />
oo~<br />
0.5 1.0 1.5<br />
FORCE N<br />
Fig. 5.28 The percent transmission of core input<br />
light obtained at the output as a function<br />
of applied force in a microbend intensitytype<br />
fiberoptic sensor.<br />
After J. Fields, et al., J. Acouat. Soc. Am. ~, 816<br />
(1980).<br />
Using the results of this and aimilar experiments,<br />
the Hughes investigatora, in cooperation with<br />
the Physical Acouatica Branch of the U.S. Naval Reaearch<br />
Labora~ory, deaigned and teated a hydrophore employing<br />
such a microbend deformer as the transducer element.<br />
Their first prototype unit ia aketched in Fig. 5.29<br />
DIAPH<br />
/-- FIBERLEADS<br />
/<br />
Fig. 5.29 A microbend intenaity-type fiberoptic sensor<br />
hydrophore developed by the Hughes Research<br />
Laboratories and the U.S. Naval Research<br />
Laboratory.<br />
After Fields and Cole, Appl. Opt. ~, 3265 (1980),<br />
(See Ref. 5 in Subsection 5.2.6). One deformer plate<br />
was rigidly mounted to the cylindrical ahell of the<br />
hydrophore while the other was attached to a thin diapragm.<br />
In addition to the through-put fiber, a second<br />
inactive fiber was included to insure that the deformer<br />
plates remain parallel during operation.<br />
At this point it would be uaeful to review<br />
some of the basic acoustical levels and unita of meaaure.<br />
Referring to Fig. 5.30, one frequently encountered<br />
acoustic reference pressure level encountered in air<br />
acouatics is 0.0002 dynea/cm2. This is the accepted<br />
5-1o
AIR ACOUSTICS<br />
REFERENCE LEVEL –––<br />
I<br />
UNDERWATER ACOUSTICS<br />
REFERENCE LEVEL . . . . . . - 1 -<br />
Fig. 5.30<br />
TT71 NEWTONIMETER 2<br />
~0 ~B 1 PASCAL (Pa)<br />
1 DYNE/CENTlMETER2<br />
DYNEICENTIMETER2<br />
20 MICRONEWTON/METER2<br />
4’0.0C02<br />
20 MICROPASCAL<br />
26 dB<br />
1 MlCRONEWTONfMETER2<br />
1 MKROPASCAL (#Pa)<br />
Pressure levels and units for comparison of<br />
underwater acoustic pressure reference<br />
levels.<br />
average minimum detectable sound pressure for humans at<br />
1000 Hz. Another is the currently accepted 1 m.lcronewton/m2<br />
or 1 micropascal (1 ~Pa) reference pressure for<br />
underwater acoustics. To compare these on a decibel<br />
scale, recall first that for a pressure ratio, P1/P2,<br />
the number of decibels, N, in dB, is defined by:<br />
N = 20 loglo P1/P2 (5.18)<br />
Since 0.0002 dynes/cm 2 is equl to 26 upa, the air<br />
acoustic reference pressure is 26 dB above the underwater<br />
reference pressure. Similarl as indicated in<br />
Fig. 5.30, a pressure of 1 dyne/cm J’ is at a level of<br />
74 dB re 0.0002 dyne/cm2 and at a level of 100 dB re<br />
1 pPa. Finally, a pressure of 1 Pa corresponds to 120<br />
dB re 1 pPa and 20 dBre 1 dyne/cm2. The table presented<br />
in Fig. 5.30 is an aid in interpreting hydrophore<br />
characteristics and in performing comparisons presented<br />
here and in later sections.<br />
Returning to the consideration of the Hughes-<br />
NRL microbend hydrophore, an experimental evaluation of<br />
the acoustic characteristic of their initial prototype<br />
was conducted at NRL. As indicated in Fig. 5.31, the<br />
hydrophone was placed in an acoustic test tank and measurements<br />
were made of its sensitivity and frequency response<br />
over a frequency range of 200 Hz to 2000 Hz. The<br />
H<br />
~<br />
MODE STRIPPER<br />
u \<br />
results are shown in graphical form in the lower por–<br />
tion of the figure. The minimum detectable pressure,<br />
in a 1 Hz band and at a unity signal-to-noise ratio,<br />
was approximately 100 dB re 1 ma. The 10 dB fluctuations<br />
about this value were attributed to resonances in<br />
the outer case and deformer mount. It should be possible<br />
to eliminate these resonances without much difficulty.<br />
In addition, a significant increase in sensitivity<br />
was achieved in later designs by employing speciallydesigned<br />
graded-index fibers. This was to be expected<br />
since the fiber employed in the initial prototype was<br />
a readily available standard communications step-index<br />
fiber. Such optical fiber has been designed to have<br />
low microbend sensitivity to reduce losses due to bending<br />
introduced in cabling and other field use distortions.<br />
By employing graded-index fibers with enhanced<br />
microbend effects, sensitivity increases of more than<br />
40 dB have been achieved. Thus, these improved microbend<br />
transducers are comparable to many of the more<br />
conventional hydrophores currently in use.<br />
It should be emphasized that with the microbend<br />
transducers discussed above, attempts are made to<br />
detect a very small change in the intensity of a relatively<br />
intense optical beam. This type of sensor is<br />
referred to as a brightfield microbend transducer. A<br />
second type of microbend device, a so called darkfield<br />
transducer, was proposed initially by a group at Catholic<br />
University and currently is under investigation by<br />
several different groups. The sensor is shown in Fig.<br />
5.32. Beginning at the left, it is quite similar in<br />
OPTICAL<br />
SOURCE<br />
Fig. 5.32<br />
FIBER<br />
DEFORMER<br />
MODE<br />
STRIPPER<br />
The microbend darkfield intensity-type fiberoptic<br />
sensor system.<br />
arrangement to the brightfield transducer up to and including<br />
the deformer. As with the brightfield transducer<br />
described above, light, possibly from a broadband<br />
incoherent source, is introduced into a multimode<br />
fiber. Care ia taken to remove cladding light prior to<br />
the deformer. The darkfield transducer differs from<br />
the brightfield transducer in that the light ejected<br />
from the core into the cladding is used to generate the<br />
output signal.<br />
Fig. 5.31 Test arrangement and sensitivity level of<br />
the Hughes Research Laboratories and U.S.<br />
Naval Research Laboratory microbend intensity-type<br />
fiberoptic senaor hydrophore.<br />
After Fields and Cole, APP1. Opt. ~, 3265 (1980)0<br />
5.1 1<br />
As indicated in Fig. 5.32, the Catholic University<br />
group used a more elaborate mode-stripper on<br />
the output section of the fiber (see Ref. 6 in Subsection<br />
5.2.6). The fiber was stripped of ita outer coating<br />
and passed through a small chamber filled with a<br />
refractive-index matching fluid. A number of photodetectors<br />
mounted in the walls of the chamber responded<br />
to changes in the intensity of the core-to-cladding<br />
ejected light. In contrast with brightfield, the darkfield<br />
case has a relatively low level of background<br />
light that is modulated by changes in displacement of<br />
the deformer. The degree” of modulation<br />
-<br />
may be quite<br />
large and thus a very high sensitivity<br />
may be employed without overdriving it.<br />
detectable signals should, in principle,<br />
in the brightfield case. This has been<br />
recent studies.<br />
photodetector<br />
The minimum<br />
be lower than<br />
confirmed in
A simplified design of the cladding light<br />
monitor is indicated in Fig. 5.33. The pick-up fiber<br />
STRIPPER<br />
I o-<br />
SOURCE FIBER<br />
DEFORMER<br />
transducer outputs could also be accomplished prior to<br />
photodetection. The optical outputs may be combined<br />
with appropriate time delays determined by the transducer<br />
spacings and coupler fiber lengths. On the other<br />
hand, by employing a pulse modulated optical source, it<br />
is possible to employ a single return bus fiber into<br />
which the optical output pulses from the various transducers<br />
could be fed. Time domain multiplexing schemes<br />
could then be used to identify and process the signal<br />
from the individual sensors. These and other various<br />
types of fiberoptic sensor arrays and the telemetering<br />
of their outputs are discussed in detail in Chapter 6.<br />
Fig. 5.33<br />
FIBER-FIBER<br />
COUPLER<br />
DETECTOR FIBER<br />
kAI<br />
A darkfield microbend intensity-type fiberoptic<br />
sensor with a fiber-fiber coupler<br />
following the deformer (microbender) developed<br />
by the Catholic University.<br />
is directly coupled to the outer surface of the cladding<br />
of the through-put fiber. Recent studies of this<br />
technique have ha~ p~omising results.<br />
darkfield<br />
The design and operation of a linear array of<br />
microbend sensors is shown in Fig. 5.34. Each<br />
This brief description of various intensity<br />
type sensors is not exhaustive. The discussion is aimed<br />
at introducing some basic concepts regarding their overall<br />
design and behavior. Many other fiberoptic intensity<br />
transducers are currently under investigation such<br />
as sensors employing fibers with temperature sensitive<br />
absorptive dopants, and several displacement and pressure<br />
transducers employing strain-induced birefringence<br />
as an intensity transduction mechanism. All of these<br />
have the advantage of being much simpler in design and<br />
operation, but they are less sensitive than interferometric<br />
fiberoptic sensors. Further improvements, including<br />
increases in sensitivity, are expected for the<br />
intensity-type fiberoptic sensors.<br />
5.2.6<br />
1.<br />
2.<br />
3.<br />
s.<br />
R.<br />
w.<br />
References<br />
Sheem and J. Cole, Opt. Lett. ~, 322 (1979).<br />
Phillips, Opt. Lett. ~, 318 (1980).<br />
Spillman, Appl. Opt. ~, 465 (1981).<br />
STR!-R<br />
DEFORMER<br />
SOURCE FIBER<br />
STRIPPER<br />
,~fi \.- .<br />
----<br />
\<br />
---<br />
-<br />
DEFORMER<br />
K /’<br />
FIBER-FIBER<br />
COUPLERS<br />
%T<br />
)<br />
Fig. 5.34<br />
A series of deformers used to control the<br />
intensity of light tapped from an optical<br />
fiber bus.<br />
sensor is an assembly consisting of a cladding-mode<br />
stripper, a microbend deformer (transducer), and a fiber-to-fiber<br />
coupler. Many of these assemblies may be<br />
mounted in series on a single optical fiber bus. The<br />
cladding-mode stripper removes any residual light in<br />
the cladding just prior to the microbend deformer. The<br />
deformer causes light from the core to enter the cladding<br />
according to the baseband (information-bearing<br />
force, pressure, or sound) signal. Following the deformer,<br />
the coupler removes the light (baseband signal)<br />
from the claddlng and dispatches it to a photodetector.<br />
A number of different multiplexing schemes<br />
could be used in the detection portion of the array.<br />
The moat direct, would be to feed each cladding light<br />
pick-up fiber to a separate photodetector. Temporal<br />
and spatial averaging of a number of closely spaced<br />
5-12<br />
4.<br />
5.<br />
6.<br />
5.3<br />
J.<br />
J.<br />
J.<br />
N.<br />
R.<br />
Fields, C. Asawa, O. Ramer, and M. Barnoski,<br />
Acoust. SOC. Am. Z, 816 (1980).<br />
Fields and J. Cole, Appl. Opt. ~, 3265 (1980).<br />
Lagakos, T. Litovitz, P. Macedo, R. Mohr, and<br />
Meister, Appl. Opt. ~, 167 (1981).<br />
<strong>FIBEROPTIC</strong> LINRAR ACCELEROMETERS<br />
The operation of interferometric fiberoptic<br />
sensors described in Section 5.1 depends primarily on<br />
phase changes associated with force-field-induced mechanical<br />
strains. Similarly the two-fiber optical accelerometer<br />
described in this section makes use of the<br />
change in fiber length due to a force resulting from<br />
the acceleration of a mass suspended between two fibers.<br />
The effect is to increase the tensile stress in the fiber<br />
in one arm of an interferometer and decrease the<br />
tensile stresa in the fiber in the other arm. The device<br />
for accomplishing this is shown in Fig. 5.35. A<br />
section of the fiber in one arm of the interferometer<br />
is attached both to the upper end of the case and to<br />
the mass. A similar section of fiber in the other arm<br />
of the interferometer is attached to the mass and to<br />
the lower end of the case. Thus, the mass, m, is suspended<br />
between the two fiber sections which effectively<br />
serve as springs. If the accelerometer case is given<br />
an acceleration, a, vertically upward, the upper fiber<br />
elongates by AL and the lower fiber shortens by the<br />
same amount in providing the force F required to accelerate<br />
the mass. This may be written as<br />
F=2AAT=ma (5.19)
Fig. 5.35<br />
SIGNAL<br />
ELECTRICAL<br />
REBALANCE<br />
UPPER<br />
~1 lppoRT<br />
IER<br />
MASS<br />
DIODE<br />
LASER<br />
3dB COUPLER<br />
iii=<br />
CASE<br />
DIAPHRAGMS<br />
LOWER SUPPORT<br />
lkFIBER<br />
)1‘t’ /u<br />
m1<br />
s<br />
3dB COUPLER<br />
PHOTODIODES<br />
A two-fiber phase-change interferometric<br />
fiberoptic accelerometer.<br />
where A is the cross sectional area of the fiber, AT is<br />
the magnitude of the change of the tensile stress in<br />
each fiber, and the 2 is due to the presence of two fibers.<br />
The resulting strain AS = .4L/L is given by:<br />
AS = AT/Y = ma/2YA (5.20)<br />
attached to a spring with a spring constant k, the resonant<br />
frequency is given by:<br />
combining Eqs. (5.26) and (5.27) there is obtain-<br />
Thus,<br />
ed:<br />
fr = (1/2n)(k/m)112. (5.27)<br />
fr = (1/2n)(2YA/Lm)l/2 (5.28)<br />
As above, A = m(d/2)2. To further emphasize the dependence<br />
of the resonant frequency, fr, on the fiber parameters,<br />
Eq. (5.28) may be written as:<br />
fr = [Yd2/8mLm]1/2 (5.29)<br />
Comparing Eqs. (5.25) and (5.29) we see that the optical<br />
fiber physical parameters appear in the form Yd2/<br />
Lm. Therefore, if the expression d2/Lm in Eq. (5.25)<br />
is decreased in order to decrease ~in, the value<br />
of fr given by Eq. (5.28) is also decreased. The minimum<br />
detectable acceleration (a~n) and longitudinal<br />
resonant frequency are shown in Figs. 5.36 and 5.37 as<br />
functions of m and d. In each case the length of fibe<br />
L is taken to be one cm and the value of A is 10 -5<br />
radian. Alternately, if a mass of one gram % ~ chosen,<br />
the mass in grams on the abscissa in both Figs. 5.36<br />
and 5.37 can be replaced by the length in centimeters.<br />
3.0 t.<br />
where Y is Young’s modulus for the fiber.<br />
Consider next an optical beam propagating in<br />
one of*the fibers. Its phase shift, $ , in traveling<br />
the length L, as given in Subsection 4.2.1 and Eqs.<br />
(4.7) and (4.8), is:<br />
4 = zn~~l~o (5.21)<br />
where h. is the optical wavelength in vacuum and n is<br />
the fiber core’s refractive index. The’ quantity Aoln<br />
is the wavelength of the light in the fiber core. In<br />
general, the change in @ per fiber (twice this for two<br />
fibers) may be written as it was in Eq. (5.1), namely:<br />
A+ = 2m(nAL + LAn)/Ao (5.22)<br />
with the wave number k = 2iI/lo. For the case of a tensile<br />
strain, however, the AL term dominates and one may<br />
write:<br />
A+ = 2nnAL/~o = 2nnLAS/lo (5.23)<br />
Fig. 5.36<br />
10.0<br />
10 2.0 3.0<br />
MASS (grams)<br />
The variation of sensitivity in micrograms<br />
as a function of the mass in grams in a<br />
fiberoptic accelerometer for different<br />
sizes of fibers.<br />
Substituting into Eq. (5.23) from Eq. (5.20) and because<br />
A - n(d/2)2:<br />
A~ = 4nLma/Y~d2 (5.24)<br />
where d is the fiber diameter.<br />
- h<br />
-$<br />
d<br />
m -1-<br />
Solving Eq. (5.24) for ~n in terms of A$~n yields:<br />
amin = AoYd2A$tin/4nLm (5.25)<br />
Referring to Fig. 5.35, the effective spring<br />
force F, required to displace the mass m a distance z,<br />
along the axis of the fiber, is given by:<br />
F = -2YAz/L = -kz (5.26)<br />
from which it follows that 2YA/L = k, where k is the<br />
effective spring constant. However, when a mass m is<br />
.--— ------.-----<br />
I 1 1 1<br />
10 2.0 3.0<br />
MASS(grams)<br />
Fig. 5.37 The variation of resonant frequency as a<br />
function of the mass in a fiberoptic accelerometer<br />
for different sizes of fibers.<br />
5-13
Referring once more to Fig. 5.35, if the mass<br />
is given a transverse (cross axis) acceleration, both<br />
optical fibers are strained the same amount. Thus, the<br />
interferometer remains balanced and to first order this<br />
device is insensitive to transverse accelerations.<br />
Cross axis coupling will occur if simultaneously there<br />
are components of acceleration that has components<br />
parallel and perpendicular to the longitudinal axis of<br />
the fiber. The diaphragms indicated in Fig. 5.35 are<br />
provided to essentially eliminate cross-axis coupling.<br />
Tveten et.al. (See Ref. 1 of Subsection 5.3.1)<br />
investigated a single fiber version of this device. The<br />
sensitivity in radians/g versus frequency is shown in<br />
Fig. 5.38 and the value of amin versus frequency in<br />
Fig. 5.39.<br />
100or<br />
y 100 -<br />
v<br />
: 10 -<br />
~<br />
> ~-----<br />
&l -<br />
:<br />
~ 0.1 1<br />
0 100 200 300 400 500<br />
5.4 <strong>FIBEROPTIC</strong> ROTATION-Fb+TE <strong>SENSOR</strong>S<br />
5.4.1 Introduction<br />
The measurement of rotation is of considerable<br />
interest in a number of areaa. For example, inertial<br />
navigation systems as used in aircraft and spacecraft<br />
depend critically on accurate inertial rotation<br />
sensors. The allowable errors in rotation sensor performance<br />
depend on the particular application. Typical<br />
requirements for aircraft navigation lie between 0.01<br />
and 0.001 degreeslhour. In terms of earth rotatio<br />
rate, flE = 15 degrees/hour, this becomes 10-3 to 10 -2<br />
!lE. Fig. 5.40 lists several other applications of rotation<br />
sensors, such as surveying, where the accurate<br />
determination of azimuth and geodetic latitude is important<br />
(see Ref. 1, Subsection 5.4.20). In this case<br />
-6 ~ or less iS needed.<br />
performance of 10<br />
Geophysics<br />
applications include 2t e determination of astronondcal<br />
latitude, and the monitoring of polar motion caused by<br />
wobble, rotation, precession and wandering effects (see<br />
Ref. 1, Subsection 5.4.20). A highly precise rotation<br />
sensor may be used to measure any changes in the length<br />
of the day and to detect torsional oscillation in the<br />
earth caused by earthquakes. Finally, ultraprecise<br />
sensors may find applications in relativity-related<br />
experiments such as the determination of the preferred<br />
frame and dragging of inertial frames (see Ref. 2,<br />
Subsection 5.4.20).<br />
FREQUENCY HZ<br />
Fig. 5.38 The sensitivity in radianslg (g = 9.8m/s2)<br />
of a single-fiber fiberoptic accelerometer<br />
as a function of frequency. The low-frequency<br />
theoretical sensitivity is shown by<br />
the horizontal line.<br />
After A. Tveten et al., Electron Lett., — 16, 854 (1980),<br />
●<br />
●<br />
●<br />
●<br />
NAVIGATION WQESIO –3<br />
SURVEYING<br />
AZIMUTH, GEODETIC LATITUDE N
● ANGULAR MOMENTUM CRYOSCOPES<br />
MECHANICAL - ROTATING WHEELIBALL<br />
NUCLEAR - SPINNING NUCLEI<br />
● SAGNAC EFFECT “GYROSCOPES”<br />
E.M. WAVES<br />
MAITER WAVES<br />
● DISTANT-STARS TRACKERS<br />
Fig. 5.41<br />
SIMPLE STAR TRACKERS<br />
LONG-BASELINE STELL4R INTERFEROMETRY<br />
Various rotation-rate sensor devices.<br />
5.4.3 Interest in Optical Rotation Sensors<br />
The main advantages of optical “gyroscopes”<br />
over mechanical ones are briefly outlined in Fig. 5.42.<br />
However, it is the promise of the projected low cost of<br />
the optical devices that is driving their development.<br />
where A is the area enclosed by the path, i.e., A = ~R2<br />
and c ia the velocity of light in a vacuum.<br />
The rigorous derivation of this formula is<br />
based on the propagation of light in a rotating frame<br />
(see Ref. 5, Subsection 5.4.20) i.e., an accelerating<br />
frame of reference, where the general theory of relativity<br />
must be used to perform the calculation. However,<br />
a simple way of explaining the formula in Eq.<br />
(5.30) iS given in Fig. 5.43. Again, consider the disc<br />
D ----------- % 1<br />
i’R,,@j<br />
,’ .<br />
2<br />
‘1 ,,, ,’<br />
‘., ,/’<br />
‘.<br />
..- --<br />
,,<br />
------<br />
Lcw=2mR+R~tcw= Ccwtcw<br />
{<br />
Lccw=27rR-R~tccw= Cc,-wtccw<br />
>tcw= ~c::RRQ<br />
~At=tcw–tccw= ‘wR<br />
IN A VACUUM CCW=CCCW=C<br />
2*R<br />
: tccw = Cccw + RQ<br />
[2R~ - (Ccw - Cccw)]<br />
Ccw ccc.<br />
Fig- 5.42<br />
● NO MOVING PARTS<br />
● No wARM-UPTIME<br />
● NO G-SENSITIVITY<br />
. LARGE DYNAMIC RANGE<br />
● DIGITAL READOUT<br />
● LOW COST<br />
● SMALL SIZE<br />
● USES LIGHT<br />
Potential advantages of optical rotationrate<br />
sensors (gyroscopes).<br />
In this section we will give a brief and<br />
ple derivation of the Sagnac effect in vacuum and<br />
in a medium; discuss techniques of implementing<br />
simalso<br />
the<br />
Sagnac effect for the measurement of rotation together<br />
with the fundamental limits on sensitivity in each case.<br />
The basic principle of fiberoptic rotation aensors will<br />
then be considered with emphasis on techniques, problem<br />
areas, and recently achieved performance.<br />
5.4.4 Sagnac Effect in a Vacuum<br />
AH the optical rotation sensors under development<br />
are based on the Sagnac effect (ace Ref. 5,<br />
Subsection 5.4.20) which generatea an optical path difference<br />
AL that is proportional to a rotation rate fl.<br />
For example, if we have a diac of radius R that is<br />
rotating with angular velocity Q, as shown in Fig. 5.43,<br />
the optical path difference AL experienced by light<br />
propagating along opposite directions along the perimeter<br />
is given by:<br />
~ At = ‘TR ~ O = %() ; ~ AL= LCW– LCCW. ~C)<br />
Fig. 5.43 A demonstration of the Sagnac relationships<br />
for the vacuum case.<br />
of radius R rotating with an angular velocity !l about<br />
an axis perpendicular to the plane of the disc. At a<br />
given point on the perimeter, designated by 1 in Fig.<br />
5.43, identical photons are sent in clockwise and counterclockwise<br />
directions along the perimeter. If Q = o,<br />
the photons, which travel at the speed of light in a<br />
vacuum, will arrive at the starting point 1 after covering<br />
an identical distance 2?TR in a time t = 2nR/c. Now<br />
in the presence of a disc rotation $2, the ccw photon<br />
will arrive at the starting point on the disc, which is<br />
now located at position 2, after covering a distance<br />
Lccw which iS shorter than the perimeter 2TR given by:<br />
L Ccw<br />
= 2TR - l?iltccw = cccwtccw (5.31)<br />
where Ri2 is the tangential velocity of the disc and<br />
tccw is the time taken to cover the distance Lccw. I n<br />
addition, Lccw is also given by the product of the<br />
velocity of light Cccw in the ccw direction and tccw.<br />
For propagation in a vacuum Cccw = C. Similarly, the<br />
photons propagating in the cw direction experience a<br />
larger perimeter Lcw given by:<br />
Using Eqs. (5.31)<br />
tccw as given In<br />
between clockwise<br />
comes:<br />
LCw = 2TR + R!ltcw = ccwtcw (5.32)<br />
At = tcw - tccw<br />
and (5.32) we can solve for tcw and<br />
Fig. 5.43 so that the difference At<br />
and counterclockwise propagation be-<br />
. (21TR)(2Rf0/C2 =<br />
(5.33)<br />
AL = (4A/c)$l (5.30)<br />
4TR2nlc2 =<br />
(4A/c2)sl<br />
5-15
The path length AL traveled by light in a time At is<br />
therefore given by:<br />
AL = cAt = (4A/c)fl (5.34)<br />
5.4.5 Sagnac Effect in a Medium<br />
In the case of light propagation in a medium<br />
(see Ref. 5, Subsection 5.4.20) of refractive index n,<br />
(Fig. 5.44) the velocity of propagation must take into<br />
consideration the relativistic addition of the velocity<br />
of light in the medium, i.e., c/n and the tangential<br />
velocity of the medium, i.e., Rfl so that Ccw becomes:<br />
Ccw = (c/n + R.Q)/(l + RQ/nc) =<br />
c/n+RQ(l- l/n2 + ...)<br />
(5.35)<br />
This<br />
given<br />
corresponds to a nonreciprocal phase shift A$,<br />
by:<br />
A$ = 2~Atc/Ao = 2rAt/(A/V)<br />
= (8.AN/aoC)c?<br />
(5.40)<br />
where A = A./n and v = c/n are the wavelength and sc.eed<br />
“.<br />
of light in the medium (n is the refractive index of<br />
the fiber core), respectively. In terms of path length<br />
difference:<br />
AL = A4A012T = (4AN/c)!l (5.41)<br />
For a fiber of length L wound in a coil of diameter D:<br />
A = TD2/4 and N = L/nD so that:<br />
AL = (4~/c)n = (LD/c)n (5.42)<br />
to first<br />
order in VIC.<br />
Similarly Cccw,<br />
is given by:<br />
or:<br />
CCCW = (c/n - IW)/(1 - RQ/nc) =<br />
c/n-RQ(l - l/n2 + ...)<br />
IN A MEDIUM. REFRACTIVE INDEX n<br />
~<br />
c<br />
+RO<br />
c . Cw = ~ +RQ (l– ~)+..<br />
1+% “2<br />
c<br />
Ti- – R()<br />
C&w = —<br />
,–~<br />
=<br />
nc<br />
c<br />
7i-<br />
–Rfl (1-~)+<br />
(5.36)<br />
AI$ = (2TTLD/aoC)Q (5.43)<br />
5.4.6 The Magnitude of the Sagnac Effect<br />
In order to get a feel for the magnitude of<br />
AL, (Fig. 5.45) assume an area A = 100 au2 and a rota-<br />
~~:~orate of 10-3 ~ (i.e., 0.015°/hr or 7 x 10-8 radl<br />
For a single-turn fiber loop enclosing such an<br />
area we get AL . 10-15 cm. This is not a very large<br />
effect considering the diameter of a hydrogen atom is<br />
about IO-8 cm. Clearly, a large number of turns N is<br />
necessary to increase the magnitude of AL.<br />
~Ccw-Cccw=2RQ (1-;)<br />
r<br />
~A, ~2wR[2R &(Ccw-Cccw)l ~ 2rR12R0-2R62(l-p)j<br />
Ccwcccw<br />
C2<br />
“2<br />
THESAME ASIN AVACUUM<br />
‘EE1<br />
Fig. 5.44 A demonstration of the Sagnac relationships<br />
for the rotating single-loop optical fiber.<br />
A=100cm2; Q .CiE * 10-4 rad/sec<br />
~ AL*10-12cm<br />
W. ‘DIAMETER- OF HYDROGEN ATOM- lo-8cm<br />
FoR n = 10-3nE = 10-7 radlsec<br />
Fig. 5.45 Computation of the change in effective optical<br />
length (Sagnac effect) in a rotating<br />
single-loop of optical fiber.<br />
Therefore, At in a medium becomes:<br />
At = tcw - tccw<br />
= 21rR[2Ro - (Ccw - cccw)l/[cc#ccwl<br />
(5.37)<br />
UPon substitution for Ccw - Cccw from above, there is<br />
obtained:<br />
At = 21TR[2RQ - 2RQ(I - l/n2]/[c2/n2]<br />
. 21TR(2RQ/C2) = (4A/c2)Q<br />
(5.38)<br />
which is idential to that in a vacuum. If the medium<br />
is an optical fiber wound in a coil of N turns, then At<br />
becomes:<br />
At = (4AN/c2)fl (5.39)<br />
5.4.7 Methods of Optical Rotation Sensin&<br />
For the sake of completeness, Fig. 5.46 shows<br />
the various schemes for the measurement of AL. On the<br />
extreme right is the multiturn fiber interferometer<br />
method (see Ref. 7, Subsection 5.4.20) mentioned above.<br />
On the extreme left is the ring laser approach (see<br />
Ref. 6, Subsection 5.4.20) and in the middle is the<br />
passive resonator approach (see Ref. 8, Subsection<br />
5.4.20). In both the active and the passive reaonator<br />
approach, a nonreciprocal path length difference AL due<br />
to the Sagnac effect becomes a nonreciprocal change in<br />
the resonance frequency, Af, of the cavity for CW and<br />
ccw propagation where:<br />
Af = (4A/ioP)$l (5.44)<br />
5-16
1<br />
1<br />
I<br />
where P is the optical perimater of tha path. In the<br />
active resonator (i.e., ring laser) approach the cw and<br />
ccw outputs of the laser have a frequency difference<br />
Af which IS auto~tically generated when the laser is<br />
JIL<br />
subjected to a rotation. In the case of the passive<br />
resonator, Af has to be measured by means of lasers<br />
external to the cavity (see Refs. 8 and 9, Subsection<br />
5.4.20).<br />
SAGNAC EFFECT I<br />
1<br />
I<br />
I<br />
ACTIVE APPROACH<br />
PASSIVE APPROACH<br />
[ r {<br />
RING LASER RESONATOR<br />
II INTERFEROMETER<br />
PHOTON SHOT NOISE<br />
c ~0/2<br />
‘jf]MFG= LD ~<br />
~<br />
Fig. 5.48<br />
Photon shot-noise computation for a multiturn<br />
fiberoptic gyroscope utilizing the<br />
Sagnac effect.<br />
fcw<br />
H<br />
Fig. 5.46<br />
fccw<br />
I-7 d<br />
( AL=!$N,,<br />
&@=bA N,,<br />
A. & -<br />
AL<br />
Methods of measuring the change in effective<br />
optical length ( Sagnac ef feet).<br />
5.4.8 Fundamental Limits in Optical Rotation<br />
Sensors<br />
Figs. 5.47 and 5.48 show a comparison without<br />
derivation of the quantum noise limit for all three<br />
cases. For the ring laser (RL) , the quantum limit comes<br />
from spontaneous emission in the gain (see Ref. 10, Subsection<br />
5.4. 20) medium and gives an uncertainty 6!l in<br />
the measurement of Sl given by:<br />
where r. is the linewidth of the ring laser cavity with<br />
no gain; nph Is the number of photons/see in the laser<br />
beam and T is the averaging time. For the passive resonator<br />
(PR) case the limit is determined by photon shot<br />
noise and is given by:<br />
6nPR<br />
= (kop/4A)(rc/(nphTl~T )1’2) (5.46)<br />
where q D is the quantum efficiency of the photodetector.<br />
As can be seen, the passive and active resonator approaches<br />
give approximately the same limit. For the<br />
multiturn fiberoptic (FO) interferometer ( see Ref. 11,<br />
Subsection 5.4. 20) the photon shot noise limit is given<br />
by:<br />
M-lFo = (c/LD) (ko/2(nph~JjT )1/2) (5.47)<br />
where nph is a number of photons/see leaving the interf<br />
erometer. Al these limits are compare -# in Fig. 5.49<br />
for A = 100 cm i ; P = 60 cm; 10 = 6 x 10 =3X<br />
1015 photons/see corresponding to 1 mW; L =c~bOn~h(i. e. ,<br />
N = L/P = 1000); rc = 300 kHz; IID = O. 3; and T = 1 sec.<br />
We notice tha the uncertainty d~ in this example is<br />
about 5 x 10<br />
-t ,E or O. 008°/hr for all three cases.<br />
6% x oioP/4A)(rc/(nphT) l’2) (5.45) RING LASER PASSIVE RESONATOR FIBER<br />
● RING LASER GYRO<br />
J-------+<br />
1<br />
I<br />
1<br />
! SPONTANEOUS<br />
EMISSION<br />
,<br />
\-~:;.+.w- fccw<br />
i<br />
fcw<br />
● PASSIVE RESONATOR GYRO<br />
t+<br />
+- + ~+<br />
4 4<br />
I<br />
fccw<br />
fcw<br />
,\cJ P I ‘~<br />
,)!! x — —<br />
RLG 4A ~<br />
~2<br />
EXAMPLE: A = 77<br />
P = To<br />
L = NP<br />
= 100 cm 2 ; Ao= 6x1O cm<br />
c AOI 2<br />
LD j=<br />
= 40 cm ; n ~h = 3x1015Isec = lmW<br />
= 400 m ; T * 1 sec<br />
rc x 300 kHz 70 = 0.3<br />
El<br />
PHOTON<br />
SHOT NOISE<br />
-t<br />
Fig. 5.47<br />
I<br />
Computation of quantum noise limits in fiberoptic<br />
rotation-rate sensors.<br />
I<br />
Fig. 5.49<br />
&f)= 4.10–4QE 7XI0 “QE 5X1O–4 f)E<br />
0.006 “/hr 0.01 “Ihr 0.008 O/hr<br />
Computation and comparison of the shot-noise<br />
limits for various types of rotation-rate<br />
sensors utilizing the Sagnac ef feet.<br />
5-17
5.4.9 Fiberoptic Rotation-Rate Sensors<br />
A simple configuration of a multiturn fiberoptic<br />
rotation-rate aensor (see Ref. 7, Subsection<br />
5.4.20) is shown in Fig. 5.50. Light from a laser or<br />
some other suitable light source ia divided into two<br />
beams by a 50-50 (3 dB) beamsplitter and then coupled<br />
into the two ends of a multiturn (multlloop) singlemode<br />
fiber coil. The light emerging from the two fiber<br />
ends is combined by the beamsplitter and detected in a<br />
photodetector. In the abaence of rotation, the two<br />
emerging beams interfere either destructively or constructively<br />
depending on the type of beamsplitter used.<br />
For a 50-50 (3 dB) lossless beamsplitter the emerging<br />
beams, as shown in Fig. 5.50, interfere destructively.<br />
Fig. 5.50<br />
d<br />
DETECTOR<br />
L –L~cw=~NQ<br />
Cw<br />
c<br />
n<br />
e,g. N=1000:A=100cm2: Q=f)E<br />
=AL~16gcm<br />
-5A<br />
=2X1O<br />
A$=8mANQs10-4 RAD<br />
Aoc<br />
NTURNS<br />
Computation of the phaae change for a multiturn<br />
fiberoptic interferometric rotationrate<br />
sensor.<br />
However, the emerging beams that return back to the<br />
light source interfere constructively, i.e., at the peak<br />
of a fringe. In the presence of a rotation rate $2, a<br />
AL will be generated given by:<br />
Typically, for a fiber attenuation rate of 1 dB/km, the<br />
optimum length is several km.<br />
5.4.10 Photon Shot-Noise Limit<br />
Earlier a proof was given of a comparison of<br />
the basic limits to the rotation measurement using the<br />
three techniques outlined in Fig. 5.46. In this section<br />
we will derive an approximate formula for the limit in<br />
a fiberoptic rotation-rate sensor.<br />
Fig. 5.51 shows a plot of intensity I or detector<br />
output current iD versus nonreciprocal phase<br />
shift A+ . In this case, the peak intensity, due to constructive<br />
interference, is shown centered on A$ = O for<br />
a zero rotation rate. In the presence of a rotation,<br />
A+ shifts from zero and therefore a change in detection<br />
current iD occurs. The greatest change in iD for a<br />
given small change in A$ clearly occurs at the point on<br />
the fringe with the maximum slope, i.e., where A$ = +<br />
~12. Therefore, by applying a fixed nonreciprocal bia~<br />
of T/2, the operating point can be maintained where the<br />
sensitivity to rotation is a maximum. In this way, an<br />
applied rotation causes a A$ which in turn generates a<br />
change in the light intensity at the detector that is<br />
proportional to the rotation. A problem arises when the<br />
1<br />
&I D<br />
,)<br />
;1<br />
,1 i<br />
,1<br />
,1<br />
INTENSITY NOISE<br />
-w OY?$7<br />
)<br />
A+<br />
8(A+)<br />
- PHOTON<br />
/ SHOT NOISE<br />
N O I S E - -<br />
8( AIP)s-= — iD/~ - iD/IT<br />
T<br />
7r<br />
*LS .—<br />
SIN iDm m<br />
*OC ~=87AN<br />
BUT A@=* —Q AOC<br />
AL = Lcw - Lccw = (4Atf/c)n = (LDIc)Q (5.48)<br />
where A, N, L, D have been defined earlier. This AL<br />
will therefore cause a fringe shift Az given by:<br />
or a phase shift of:<br />
AZ = (LD/ioC)n (5.49)<br />
A$ = (21TWaoC) (5.50)<br />
For A = ~D2/4 = 100 cm2 and N = L/rD = 1000 (i.e., D<br />
‘11.3 cm and Lx 355 meters) and if i. = 0.63 ~m and<br />
n= 1.5, we get a phase shift of 3.0 rad for a rotation<br />
rate of 1 rad/sec. Therefore, to detect the full earth<br />
rotation, we must measure a phase shift of 9.1 x 10-5<br />
radians and for typical navigation applicat ons (10-3<br />
~) the phase ahift reduces to about 10 -{ radians.<br />
For a given size sensor, i.e., a fixed coil<br />
diameter D, the sensitivity may be enhanced by increasing<br />
the length of the fiber L by adding more turns. Unfortunately<br />
L cannot be increased indefinitely because<br />
of the finite attenuation of optical power in the fiber.<br />
Fig. 5.51<br />
The optical intensity (power) or photodetector<br />
output current as a function of<br />
phase change and photon shot-noise computation<br />
in a fiberoptic rotation-rate sensor.<br />
intensity of the light source varies since this cannot<br />
be distinguished from a change in intensity due to a<br />
rotation. Therefore, the uncertainty in the measurement<br />
of a given rotation rate, i.e., a given A$, must<br />
be influenced by the intensity noise in the light. M-<br />
though there are many ways of compensating for intensity<br />
variations of the light source, it is not, however,<br />
possible to reduce the effect of photon shot noise (see<br />
Ref. 12, Subsection 5.4.20) because it is a random proceas.<br />
Therefore under ideal conditions the uncertainty<br />
in the measurement of A$ ia limited only by the photon<br />
ahot noise (see Ref. 12, Subsection 5.4.20). This uncertainty<br />
6(A$) is therefore given by:<br />
6(A$) = (photon shot noise)/(fringe alope) (5.51)<br />
5-18
This is a minimum where the fringe slope is a maximum.<br />
In other words:<br />
15(A$) z n(2eiDB) qiD .<br />
iT(nph~DT )1’2/nph~DT<br />
(5.52)<br />
where e iS the electron charge; B is the bandwidth of<br />
the detection system; nph is the number of photonsfsec<br />
falling on the detector; ~ is the quantum efficiency of<br />
the detector; and T is the averaging time = l/2B. Since<br />
Eq. (5.50) iS:<br />
A+ = 2nLD/loc<br />
the uncertainty in the measurement of ~, i.e., 6$2, becomes:<br />
62 = Aoc&(A41)/21rLD<br />
Fig. 5.53<br />
JtL<br />
o ‘ $7 A#J—<br />
I/<br />
iii-<br />
-7r 0 r 4#J—<br />
Two DC methods for measurement of phase<br />
change, LO, in a fiberoptic rotation-rate<br />
sensor.<br />
which : s the same expression given earlier.<br />
5.4.11<br />
= (C/LD)(lo/2)/(nphtlT)l’2 = (5.53)<br />
cio/2LD(iD/2eB)112<br />
Ideal Performance<br />
The ideal performance of a fiberoptic “gyro”<br />
may be summarized as shown in Fig. 5.52. The random<br />
drift : s limited by photon shot noise and there should<br />
not be any aource of bias or drift in the absence of<br />
rotation. For a given rotation, the stability of the<br />
scale factor, i.e., 2nLD/aoc, which related !2 to Ah<br />
must be limited by the stability of L, D and ~o.<br />
A much better method is to use an a.c. modulation<br />
scheme employing nonreciprocal phase dither (see<br />
Ref. 11, Subsection 5.4.20) as shown in Fig. 5.54. The<br />
requirements for optimum operation are that the amplitude<br />
of the phase modulation should be + r/2 and the<br />
rate of the modulation should be high enou~h so that the<br />
detector noise is dominated by photon shot noise. Fig.<br />
5.55 is a sketch of a typical noise spectrum of a laser<br />
showing the large “l/f” noise component at low frequencies.<br />
The start of the ahot-noise-limited region depends<br />
on the particular light source and can be any<br />
where from a few kHz to a few hundred kHz. Using such<br />
●<br />
RANDOM DRIFT IS LIMITED BY PHOTON SHOT NOISE<br />
.MODULATION METHODS<br />
●<br />
●<br />
Fig. 5.52<br />
5.4.12<br />
NO BIAS OR DRIFT WHEN!! =0<br />
SCALE FACTOR STABILITY IS LIMITED BY STABILITY OFL,D<br />
ANDAO<br />
Ideal performance features of a fiberoptic<br />
rotation-rate sensor (L = coil length, D =<br />
diameter, and i. = source wavelength).<br />
Measurement of Nonreciprocal Phase Shift<br />
In order to reach the ideal performance disthe<br />
previous section, a number of problems<br />
cussed in<br />
must be overcome. The measurement of nonreciprocal<br />
phase shift A@ with an uncertainty that is limited only<br />
by the photon shot noise will now be described.<br />
A simple way of measuring A$ is illustrated<br />
in Fig. 5.53, where a T/2 bias is applied so as to operate<br />
at the point of maximum slope. In thia way an increase<br />
in intensity correaponda to a negative A$ and<br />
vice veraa. Among the disadvantages of this method is<br />
the stability of the bias and the need to compensate for<br />
laser intensity fluctuations. A better method might be<br />
to employ a differential scheme in which two detectors<br />
are placed astride a fringe as ahown in the lower diagram<br />
of Fig. 5.53. l%is scheme has twice the sensitivity<br />
of the first, and better discrimination againat<br />
intensity variations. However, it still suffers from<br />
the instability of the operating points and requires<br />
high common mode rejection.<br />
Fig. 5.54<br />
I<br />
I<br />
‘D<br />
\,& .+<br />
REQUIREMENTS:<br />
-w ; o : w<br />
● AMPLITuDE*r/2<br />
e~NONRECIPROCAL<br />
PHASE MODULATION<br />
cRATE – HIGH ENOUGH TO GIVE SHOT-NOISE LIMIT<br />
AC measurement of phase change, A$, in a<br />
fiberoptic rotation-rate sensor.<br />
It<br />
INTENSITY<br />
NOISE<br />
PHOTON 1 ——-—-——<br />
SHOT —<br />
NOISE<br />
o f—<br />
Fig. 5.55<br />
Atypical intensity-noise spectrum of a<br />
laser showing inverae frequency (l/f) and<br />
phase noise.<br />
5-19
a modulation scheme, the output of the photodetector is<br />
demodulated in a phase-sensitive demodulator followed<br />
by a low-pass filter. In this way a zero output is obtained<br />
at A$ . 0, a positive voltage for A+< O and a<br />
negative voltag e<br />
for A$ > 0. The main advantages of the<br />
modulation method are that the peak of the interference<br />
pattern is used as the reference point (i.e., no need<br />
for external offset) and that the null point is independent<br />
of intensity fluctuations as long as the modulation<br />
rate 1S high enough as mentioned above.<br />
5.4.13 Methods of Nonreciprocal Phase Modulation<br />
The various possibilities for achieving nonreciprocal<br />
phase modulation at high rates will now be<br />
described. The phase shift $ that light experiences in<br />
propagating along a single-mode fiber of length L and<br />
refractive index n (Fig. 5.56) given by:<br />
~ = 2~fnL/c (5.54)<br />
where f 1S the frequency of the light in Hz and c is<br />
the velocity of light in a vacuum. It should be noted<br />
that the magnitude of $ does not depend on the direction<br />
of propagation so that $Cw = $Ccw = $. This implies<br />
that if L, n, or f is varied, a nonreciprocal phase<br />
shift cannot be generated.<br />
Therefore, in order to generate a nonreciprocal<br />
phase shift, either Lcw ~ Lccw or ncw $ nccw or fcw<br />
+f Ccw”<br />
c<br />
but suffers from the fact that orthogonally polarized<br />
beams propagating in the fiber do not experience the<br />
aame index thus generating a temperature dependent bias.<br />
Another method of making ncw # nccw makes use<br />
of the Faraday effect either in the main fiber coil or<br />
In a separate length of fiber. By applying a longitudinal<br />
magnetic field to the fiber it is possible to cause<br />
the index for right circularly polarized light to be<br />
different from that for left circularly polarized light.<br />
Even though the Verdet constant, i.e., the constant of<br />
proportionality between magnetic field strength and index<br />
difference, is small, it can be enhanced considerably<br />
by using a longer length of fiber. Again, this<br />
scheme has been demonstrated recently (see Ref. 14, Subsection<br />
5.4.20).<br />
Yet another nonreciprocal index scheme that<br />
has enjoyed much popularity is the time delay modulation<br />
method (see Ref. 15, 16, 17, and 18, Subsection<br />
5.4.20), illustrated in Fig. 5.57. In this case advantage<br />
is taken of the comparatively long time the photons<br />
spend in the fiber. A typical scheme would be to<br />
A /<br />
“ @~w - 4CCW = ~ fn (Lcw – Lccw)<br />
* ‘/’<br />
OUTPUT<br />
‘D<br />
2T fL (ncw – ‘Ccw)<br />
● 4CW - @ccw ‘ ~<br />
14’ Cw – $Ccw ~ 2$0 SIN (2T fm ~)<br />
I<br />
“ 4CW - 4CCW = gn Ufcw - fccw)<br />
Fig. 5.56 Various possibilities<br />
phase modulation.<br />
for nonreciprocal<br />
One possibility of making Lcw ~ Lccw whether<br />
In a medium or in a vacuum is to mechanically dither the<br />
interferometer at a high angular rate so that the Sagnac<br />
ef feet itself resulting from this motion can provide the<br />
necessary nonreciprocal phase ahift. This method has in<br />
fact been used in early fiber gyros (see Ref. 13, Subsection<br />
5.4. 20) but is clearly not very desirable in<br />
general.<br />
In order to generate a nonreciprocal refractive<br />
index, i.e. , ncw # n ccw there me a number of methods<br />
that could be used. A simple scheme would be to<br />
make the polarization of, say, the cw beam orthogonal<br />
to the polarization of ccw beam and then use an electrooptic<br />
(E/0) phase modulator to generate a polarizationdependent<br />
refractive index. Such a scheme has been discussed<br />
and demonstrated ( see Ref. 11, Subsection 5.4. 20)<br />
Fig. 5.57<br />
AMPLITUDE OF<br />
PHASE MODULATION<br />
‘f FOR fm = &<br />
The time-delay modulation method for a nonreciprocal<br />
fiberoptic rotation-rate sensor.<br />
pla~e a phase modulator near the beamsplitter as shown<br />
in Fig. 5.57. The phase modulator can be constructed<br />
in many ways, such as an electrooptic crystal, or a fiber<br />
wound around a PZT. Now if the phase modulator is<br />
driven at a frequency fm it is then possible to generate<br />
a nonreciprocal phase shift given by ( see Ref. 18,<br />
Subjection 5.4.20):<br />
r$cw - $Ccw . 2@05in(2nfmTD/2) (5.55)<br />
where $0 is the magnitude of the reciprocal phase shift<br />
generated by the phaae modulation and T ~ is the delay<br />
time in the fiber which is given by nL/c. To maximize<br />
the nonreciprocal phase shift it is necessary to make<br />
the argument of the sin function = n/2 i.e. , by choosing<br />
fm = 112 ~. If fm is less than l/2TD, $0 has to be<br />
increased to achieve the appropriate amplitude of the<br />
nonreciprocal phase shift. For a 1 km fiber the optimum<br />
f m is about 100 kHz.<br />
5-20
The generation of nonreciprocal phase modulation<br />
by the frequency method will now be described (see<br />
Refs. 11 and 18, Subsection 5.4.20). In this scheme<br />
fcw is made different from fccw so that:<br />
@ Cw -0 Ccw<br />
= (2nnL/c)(fcw - fccw) (5.56)<br />
A simple way of implementing this method is by employing<br />
two acoustooptic (A/0) frequency shifters placed<br />
symmetrically on either side of the beamsplitter within<br />
the interferometer. By driving the A/O with independent<br />
oscillators it is possible to generate both nonreciprocal<br />
phaae modulation as well as fixed nonreciprocal<br />
phase shifts. For example, In a 1 km fiber a frequency<br />
difference fcw - f ccw of 50 kHz generates a nonreciprocal<br />
phase shift of T/2.<br />
Related frequency methods have also been investigated<br />
(see Refs. 19 and 20, Subsection 5.4.20).<br />
5.4.14 Open Loop and Closed Loop Operation<br />
The open loop sensor system is shown in Fig.<br />
5.58 where a nonreciprocal phase modulator (NRPM) is<br />
placed near one fiber end and driven at fm. The output<br />
of the photodetector is then demodulated at fm in<br />
a phase senaitive demodulator. After low pass filtering<br />
the demodulator output is a sinusoidal function of<br />
At as illustrated in Fig. 5.58. For any given A$, a<br />
d.c. voltage output is obtained which is proportional<br />
to A$. The disadvantages of the open loop system include<br />
(a) the calibration of the demodulator output<br />
since this depends on the gains of the various amplifiers<br />
that precede it as well as on the intensity of<br />
the light source and (b) the nonlinear behavior of the<br />
demodu~ator output with A$.<br />
1,<br />
T<br />
II<br />
NRPT<br />
LIGHT NRPM I<br />
1. — A II<br />
I<br />
w fm<br />
l--cl<br />
~ETEcToRL A —<br />
Fig. 5.59<br />
I<br />
/<br />
NULL<br />
DEMOD<br />
OUTPUT<br />
-u Smo<br />
*<br />
Closed-loop nonreciprocal phase modulation<br />
in a fiberoptic rotation-rate sensor.<br />
‘She advantages of the closed loop system over<br />
the open loop system include (a) the output is independent<br />
of light source intensity variations since the system<br />
ia always operated at null (the modulation frequency<br />
must be high enough to reach the photon shot noise);<br />
(b) the output is independent of the gains of individual<br />
components in the measurement system as long as a very<br />
high open-loop gain is maintained; and (c) the output<br />
linearity and stability depends only on the NRPT.<br />
The NRPT could, for example, be a Faraday effect<br />
device or an acoustooptic frequency shifter. If a<br />
Faraday device is used, then the stability depends on<br />
the stability of the length of the fiber and the atability<br />
of the magnetic-field/phase-shift transfer function.<br />
However, if the NRPT is an acoustooptic crystal,<br />
then a frequency difference Af = fcw - fccw is generated<br />
to offset a A$ = (21TLD/loC)n caused by a rotation.<br />
Therefore:<br />
A+<br />
LIGHT<br />
SOURCE<br />
DETECTOR<br />
OUTPUT I<br />
wAIP<br />
which implies that:<br />
A+ = 2rAfnL/c = (21TLD/aoC)il (5.57)<br />
Af = (D/nAo)!2 (5.58)<br />
Eq. (5.58) indicates that the scale factor stability<br />
depends on the coil diameter D, n, and ~. If the numerator<br />
and denominator of Eq. (5.58) is multiplied by<br />
nD/4, then:<br />
Fig. 5.58<br />
Open-loop nonreciprocal phase modulation in<br />
a fiberoptic rotation-rate sensor.<br />
In the closed loop system (see Refs. 11 and<br />
18, Subsection 5.4.20), shown in Fig. 5.59, the output<br />
of the demodulator is passed through a servo amplifier<br />
which then drives a nonreciprocal phase transducer<br />
(NRPT) placed within the fiber interferometer. In this<br />
way, the sensor is always operated at null, i.e., at<br />
A+ = O by generating a suitable nonreciprocal phase<br />
shift in the NRPT that is equal to but opposite in sign<br />
to that generated by a rotation 0. The output of the<br />
system ia then the output of the NRFT. Therefore, the<br />
NRFT becomes a critical element.<br />
Af = [(nD2/4)/(nlomD/4)]~ = (4A/XoP)fl (5.59)<br />
where P is the optical perimeter = nTD of the fiber<br />
coil. It should be noted that Eq. (5.59) is identical<br />
with Eq. (5.44) for either the ring laser or the passive<br />
reaonator approach.<br />
5.4.15 Problems in Fiberoptic Rotation Sensors<br />
So far the basic principles of fiber rotationrate<br />
sensors with emphasis on the measurement of small<br />
nonreciprocal phase shift in a multiturn fiber interferometer<br />
have been described. A number of error aources<br />
that can influence the performance of the fiber gyro<br />
will now be described briefly.<br />
5-21
Fig. 5.60 lists several sources of error that<br />
must be dealt with in order to achieve the predicted<br />
performance. Perhapa the major source of noise is backscattering<br />
within the fiber (see Ref. 21, Subsection<br />
5.4.20) and at interfaces, particularly in a setup that<br />
employs discrete components. To overcome this problem,<br />
researchers have used broadband lasers (see Ref. 17 and<br />
22, Subjection 5.4.20), frequency jittered lasers (see<br />
Ref. 18, Subsection 5.4.20), phase modulators, (see Ref.<br />
23, Subsection 5.4.20), and even light-emitting diodes<br />
(LED) (see Ref. 24, Subsection 5.4.20). By destroying<br />
the temporal coherence of the light source the detection<br />
system becomes sensitive only to the interference be-<br />
5.4.16 Integrated Fiber “Gyros”<br />
Although the early investigation of fiberoptic<br />
“gyros” employed (see Refs. 19, 30, 32 and 33, Subsection<br />
5.4.20) discrete optical components for convenience,<br />
it is clear that if fiber gyros are to make a<br />
large impact an integrated (see Ref. 34, Subsection<br />
5.4.20) optical system (Fig. 5.61) with a semiconductor<br />
laser/LED as a light source must be uaed. Beamsplitters<br />
can be replaced by either waveguide or fiber 3-dB couplers<br />
(see Ref. 17, Subsection 5.4.20). Nonreciprocal<br />
RAYLEIGH SCAITERING IN FIBER<br />
SCAITERING FROM INTERFACES<br />
POLARIZATION EFFECTS<br />
PRESENCE OF HIGHER ORDER MODES<br />
TEMPERATURE GRADIENTS<br />
NONIDEAL MODULATORS<br />
NONIDEAL POLARIZERS<br />
INTENSITY DEPENDENT NONRECIPROCITY<br />
LIGHT SOURCE PROBLEMS<br />
MEASUREMENT SYSTEM PROBLEMS<br />
STRESS INDUCED EFFECTS<br />
MAGNETIC FIELD EFFECT<br />
Fig. 5.60 Sources of noise and errors that must be<br />
considered in the design of a fiberoptic<br />
rotation-rate sensor.<br />
tween waves that followed identical counter-propagating<br />
paths. Thus, interference due to backacattering will,<br />
in principle, average to zero.<br />
The problem that has received much attention<br />
both theoretically (see Refs. 25 and 26, Subsection<br />
5.4.20) and experimentally (see Ref. 17, Subsection<br />
5.4.20) is the error due to the polarization behavior<br />
of the optical fiber. By uaing polarizers to establish<br />
the axis of polarization (see Ref. 26, Subsection<br />
5.4.20) in the long-fiber interferometer, it has been<br />
possible to reduce polarization-dependent errors. The<br />
use of the now available single-mode polarization-preserving<br />
fibers (see Ref. 27, Subsection 5.4.20) may<br />
turn out to be a convenient solution.<br />
4I<br />
Fig. 5.61<br />
I<br />
Q=POuTpuT<br />
f~<br />
NR MODULATOR<br />
An open-loop integrated fiberoptic rotation-rate<br />
sensor employing a phase transducer.<br />
phase modulators may employ a short length of fiber<br />
wound around a PZT, the Faraday ef feet, an integrated<br />
Bragg cell, or other features.<br />
Integrated polarizers (see Ref. 17, Subsection<br />
5.4. 20) and polarization controllers (see Ref. 17,<br />
Subsection 5.4. 20) are also feasible. In the closed<br />
loop approach shown in Fig. 5.62 the nonreciprocal<br />
phaae transducer could be a Bragg cell, a Faraday effect<br />
device, or other device. In other words various<br />
possibilities exist for constructing a solid-state fiber<br />
gyro. An all-optical-fiber open-loop system has<br />
already been demonstrated with a very promising performance<br />
(see Ref. 17, Subsection 5.4.20).<br />
All the fiber gyros under study so far have<br />
used single mode fibers. Care has to be taken to insure<br />
that higher order transverse modes are highly attenuated.<br />
A number of error sources are related to temperature<br />
gradients, (see Ref. 28, Subsection 5.4.20)<br />
non-ideal polarizers, (see Ref. 29, Subsection 5.4.20)<br />
non-ideal modulators, stress induced effects, external<br />
magnetic field effects (see Ref. 30, Subsection 5.4.20)<br />
and electronics problems in the measurement system.<br />
A very basic source of nonreciprocal phase<br />
shift has been uncovered, namely that due to unequal<br />
intensities propagating along opposite directions in<br />
the fiber (see Ref. 31, Subsection 5.4.20). This is a<br />
nonlinear optical effect based on four-wave mixing that<br />
takes place in a fiber having a third order nonlinear<br />
susceptibility. Such an intensity-induced nonreciprocity<br />
may be reduced by maintaining equal intensities<br />
in the counterpropagating beam.<br />
5-22<br />
Fig. 5.62<br />
I<br />
SERVO<br />
DETECTOR<br />
f~<br />
A closed-loop integrated fiberoptic rotaa<br />
tion-rate sensor employing<br />
phase trans-<br />
ducer.
5.4.17~<br />
Once the various noise mechanisms in fiber<br />
gyros were uncovered and understood, published performance<br />
data began to improve rapidly. Fiber gyros employing<br />
several hundred meters of fiber wound around a coil<br />
of 15 to 20 cm in diameter have demonstrated short term<br />
drifts in the range of 0.1 - O.01”/hr for averaging<br />
times of about 10 seconds (see Refs. 17 and 18, Subsection<br />
5.4.20). Long term drift of O.lO/hr for more than<br />
one hour has also been demonstrated (see Refs. 17 and<br />
18, Subsection 5.4.20).<br />
5.4.18 Summary of Rotation-Rate Sensors<br />
In summary, fiberoptic rotation sensors have<br />
demonstrated promising preliminary performance. However<br />
most of the causes of short term noise are understood,<br />
the causes of long term drift need further study. Clearly,<br />
the emphasis must now be placed on integrated device<br />
development.<br />
5.4.19 General Conclusions Regarding Fiberoptic<br />
Sensors<br />
It may be concluded for this entire chapter<br />
that fiberoptic sensors demonstrate tremendous potential<br />
for application in any area that requires the sensing<br />
of physical parameters, including electric fields,<br />
magnetic fields, forces, temperature, pressure, linear<br />
and rotation displacements, velocities, and accelerations.<br />
Application areas include navigation, medical<br />
engineering, surveying, transportation, telemetry (communication),<br />
in fact, any area in which measurements<br />
are to be made.<br />
5.4.20 References<br />
1.<br />
2.<br />
3.<br />
4.<br />
5.<br />
6.<br />
7.<br />
8.<br />
9.<br />
10.<br />
D.H. Eckhardt, Proc. Soc. Photo-Opt. Instru. Eng.<br />
~, 172 (1978).<br />
M.O. Scully, in Proc. of the Fifth International<br />
Conf. on Laser Spectroscopy, H. Walther and K.<br />
Rothe, eds. (Springer-Verlag, Berlin, 1979); M.P.<br />
Haugan, M.O. Scully, and K. Just, Phys. Lett. ~,<br />
88 (1980).<br />
J.H. Simpson, Astron. & Aeron. ~, #10, 42 (1964).<br />
G. Sagnac, Compt. Rend=, 708 (1913).<br />
E.J. Post, Rev. Mod. Phys. 39, 475 (1967). —<br />
A.H. Rosenthal, J. Opt. Soc. Am. ~, 1143 (1962).<br />
V. Vali and R.W. Shorthill, Appl. Opt. ~, 1099<br />
(1976).<br />
S. Ezekiel and S.R. Balsamo, Apply Phys. Lett. 30, —<br />
478 (1977).<br />
G.A. Sanders, M.G. Prentiss and S. Ezekiel, Opt.<br />
Lett. ~, 569 (1981).<br />
T.A. Dorschner, H.A. Haus, M. HoIz, I.W. Smith,<br />
and H. Stata, IEEE. J. Quant. Electron, QE-16,<br />
1376 (1980).<br />
13.<br />
14.<br />
15.<br />
16.<br />
17.<br />
18.<br />
19.<br />
20.<br />
21.<br />
22.<br />
23.<br />
24.<br />
25.<br />
26.<br />
27.<br />
28.<br />
29.<br />
30.<br />
31.<br />
32.<br />
33.<br />
34.<br />
G. Pircher, M. Lacombat and H. Lefevre, Proc. Soc.<br />
Photo-Opt. Instrum. Eng. 157, 212 (1978). —<br />
W.C. Davis, W.L. Pondrom and D.E. Thompson, Proc.<br />
of International Conf. on Fiberoptic Rotation Sensors,<br />
M.I.T., (Nov. 1981), Springer-Verlag (to be<br />
published).<br />
H. Arditty, M. Papuchon, K. Thyagarapan, and C.<br />
Puech in Digest or Topical Meeting on Integrated<br />
and Giroled-Wave Optics, O.S.A. Meeting, Washington,<br />
D.C. (1980).<br />
R. Ulrich, Opt. Lett. ~, 173 (1980).<br />
R.A. Bergh, H.C. Lefevre and H.J. Shaw, Opt. Lett.<br />
~, 502 (1981).<br />
J.L. Davis and S. Ezekiel, opt. Lett. g, 505<br />
(1981).<br />
D.E. Thompaon, D.B. Anderson, S.K. Yao and B.R.<br />
youmans, Appl. Phys. Lett. — 33, 940 (1978).<br />
R.F. Cahill and E. Udd, Opt. Lett. ~, 93 (1979).<br />
C.C. Cutler, S.A. Newton, and H.J. Shaw, Opt. Lett.<br />
~, 488 (1980).<br />
R. Ulrich, Opt. Lett. ~, 173 (1980).<br />
K. Bohm, P. Ruaser, E. Weidel and R. Ulrich, Opt.<br />
Lett. ~, 64 (1981).<br />
K. Bohm, P. Marten, K. Petermann, E. Weidel and<br />
R. Ulrich, Electon. Lett. ~, 352 (1981).<br />
R. Ulrich, Proc. of International Conf. on Fiberoptic<br />
Rotation Sensors, M.I.T. (November, 1981),<br />
Springer-Verlag (to be published).<br />
G. Schiffner, W.R. Leeb, H. Krammer and J. Wittmsn,<br />
Appl. Opt. 18, 2096 (1979). —<br />
I.p. Kaminow, J. Quant. Elect. Q.E.-17, 15 (1981).<br />
D.M. Shupe, Appl. Opt. 19, 654 (1980). —<br />
E.C. Kintner, Opt. Lett. ~, 154 (1981).<br />
K. Bohm, K. Petermann and E. Weidel, Opt. Lett. ~,<br />
180 (1982).<br />
S. Ezekiel, J.L. Davis and R. Hellwarth, Proc. of<br />
International Conf. on Fiberoptic Rotation Sensors,<br />
M.I.T. (Nov. 1981), Springer-Verlag (to be<br />
published).<br />
R. Goldstein and W.C. Rnss, Proc. Soc. Photo-Opt.<br />
Instrum. Eng. 157, 122 (1978).<br />
M.N. McLandrich and H.F. Rast, Proc. Soc. Photo-<br />
Opt. Instrum. Eng. ~, 127 (1978).<br />
M. Papuchon and C. Puech, Proc. Soc. Photo-Opt.<br />
Instrum. Eng. 157, 218 (1978). —<br />
11.<br />
12.<br />
J.L. Davis and S. Ezekiel, Proc. Soc. Photo-Opt.<br />
Instrum. Eng. 157, 172 (1978). —<br />
A. Yariv, “Introduction to Optical Electronics”,<br />
Holt, Rinehart, & Winston, (1976).<br />
5-23
CHAPTER 6<br />
<strong>FIBEROPTIC</strong> <strong>SENSOR</strong> ARRAYS<br />
AND TELEMETRY SYSTEMS<br />
Ease of multiplexing and modulation and the<br />
fundamental properties of lightwaves and optical fibers<br />
make them suitable for use in multisensory uniform and<br />
random arrays for many different applications. This<br />
chapter will cover the important characteristics of sensor<br />
arrays, their connection into telemetry systems for<br />
transmission of baseband data within the array, and the<br />
characteristics of fiberoptic transmission lines for<br />
telecommunication systems.<br />
6.1 <strong>FIBEROPTIC</strong> <strong>SENSOR</strong> ARRAYS<br />
6.1.1 Fiberoptic Sensor Array Design<br />
Considerations<br />
6.1.1.1 General Design Considerations<br />
The sensor system selected for a particular<br />
application will depend on many considerations. For<br />
example, the individual sensors that are selected depend<br />
on the parameter to be sensed, the sensitivity re -<br />
quired, the dynamic range of the parameter to be sensed,<br />
the baseband frequencies, and the noise and Power<br />
levels. The geographic distribution of the sensors in<br />
an array will be governed by the distribution of locationa<br />
at which parameters are to be aenaed. Other<br />
variables to be selected are the modulation scheme and<br />
whether an analog or a digital form will be used for a<br />
particular application. These and other considerations<br />
may be summarized as follows:<br />
used, and the telemetry methods that are used. Design<br />
aspects differ from one basic configuration to another,<br />
therefore detailed design aspects will be discussed in<br />
the next subsection, Fiberoptic Sensor Array Basic Configurations.<br />
6.1.2~<br />
The method of energizing an array and the<br />
type of fiberoptic sensors used in the array are often<br />
interrelated. For example, suppose an array of baseband-modulated<br />
darkfield microbend sensors are each<br />
sequentially mounted on a single fiber and each is preceded<br />
by a mode-stripper in such a manner that each<br />
microbend sensor of the baseband signal causes an amount<br />
of light proportional to the baseband signal amplitude<br />
to enter the cladding. Following each microbender is<br />
a tap designed to remove this baseband signal from the<br />
cladding and send it via the tap (coupler) to a common<br />
return bus. The return bus output signals may be<br />
photodetected as shown in Fig. 6.1. If the array is<br />
PULSED<br />
LIGHT<br />
SOURCE<br />
(LASER) 1<br />
MODE STRIPPER<br />
MODE STRIPPER<br />
<strong>FIBEROPTIC</strong> <strong>SENSOR</strong> ARRAY DESIGN CONSIDERATIONS<br />
<strong>SENSOR</strong> TYPE<br />
Intensity Modulation<br />
Phase Modulation<br />
Frequency Modulation<br />
Polarization Modulation<br />
Wavelength Modulation<br />
DISTANCE BETWEEN <strong>SENSOR</strong> ELEMENTS<br />
ANALOG VS DIGITAL TRANSMISSION<br />
SIMPLEX, DUPLEX, MULTIPLEX, OR COMBINATION<br />
SIGNAL PROCESSING REQUIREMENTS<br />
<strong>SENSOR</strong>/LINR CALIBRATION REQUIREMENTS<br />
POWER LEVELS<br />
SYSTEM NOISE<br />
NUMEER OF <strong>SENSOR</strong> CHANNELS<br />
MAXIMUM FREQUENCY OF SIGNAL INFORMATION<br />
OPERATIONAL NOISE ENVIRONMENT<br />
SIGNAL DYNAMIC RANGE<br />
<strong>SENSOR</strong> LEAD LENGTHS<br />
DESIRED TRANSMISSION SCHEME<br />
DESIRED MULTIPLEXING<br />
6.1.1.2 Specific Design Considerations<br />
Detailed design considerations for a fiberoptic<br />
sensor array and associated telemetry depend on<br />
the method of energizing the array, the type of sensor<br />
6-1<br />
DETECTOR<br />
Fig. 6.1<br />
TAP TAP TAP<br />
BUS COUPLERS<br />
A fiberoptic darkfield microbend sensor array<br />
telemetry system with single return bus.<br />
a linear array of equally spaced sensors and the optical<br />
feed bus is pulsed, the pulses on the return bus<br />
will be automatically time-division multiplexed for<br />
the return telemetry. If the sensors are not equally<br />
spaced and the amount of fiber required to create<br />
equal spacing is excessive, the arrangement shown in<br />
Fig. 6.2 can be used. The source output is continuous<br />
in this case. Each microbend cladding mode stripper<br />
output is fed to a separate photodetector via an independent<br />
optical fiber as shown in Fig. 6.2. Return<br />
telemetry for both of these arrangements is discussed<br />
below in greater detail. Both of these arrangements<br />
make use of darkfield sensing.
CONTINUOUS<br />
LIGHT<br />
MODE<br />
STRIPPER<br />
. .<br />
: : . .<br />
MICROBEND <strong>SENSOR</strong> ARRAY<br />
MODE STRIPPER<br />
STRIPPER<br />
,<br />
energized and either the return optical cables are each<br />
returned to a photodetector in an array, or the return<br />
bus may be a single optical cable with time-division<br />
multiplexed signals from equally-spaced sensors fed to<br />
a single photodetector as discussed earlier.<br />
The sensor array can also consist of an array<br />
of optical grating sensors that modulate the output of<br />
individually-coupled light sources (LEDs) powered by<br />
light pulses on a common electrical bus as shown in<br />
Fig. 6.5. The grating outputs are individually coupl-<br />
Fig. 6.2<br />
A fiberoptic darkfield microbend sensor array<br />
telemetry system with multiple cable<br />
return.<br />
ELECTRICAL POWER BUS<br />
><br />
I<br />
Brightfield sensing can also be accomplished<br />
in a fiberoptic sensor array as shown in Fig. 6.3. A<br />
STAR COUPLER<br />
I<br />
.<br />
CONTINUOUS \ .)<br />
:<br />
fl “ ‘<br />
PHOTODETECTOR<br />
ARRAY<br />
Fig. 6.5<br />
))<br />
A fiberoptic optical grating electricalbua-fed<br />
senaor array telemetry system.<br />
Fig. 6.3<br />
DETECTOR<br />
ARRAY<br />
)<br />
: MICROBEND BRIGHTFIELD<br />
<strong>SENSOR</strong> ARRAY<br />
A fiberoptic microbend brightfield starcoupler-fed<br />
sensor array telemetry system.<br />
star coupler is fed by a continuous light source, e.g.,<br />
a laser or an LED. Each output of the star-coupler is<br />
fed to a baseband-modulated microbend fiberoptic brightfield<br />
sensor. The output signal of each fiberoptic<br />
sensor in the array is separately fed to an array of<br />
photodetectors for further processing and transmission.<br />
~so, an electrical power bus to a light source (LED)<br />
at each sensor can be used to energize the basebandmodulated<br />
microbend fiberoptic brightfield sensor as<br />
shown in Fig. 6.4. The electrical bus is continuously<br />
LIGHT SOURCE<br />
ELECTRICAL POWER BUS<br />
)<br />
‘“Ḟ .<br />
I<br />
(LED) (LED) (LED)<br />
. ● MICROBEND <strong>SENSOR</strong><br />
.<br />
. ARRAY<br />
.<br />
.<br />
.<br />
.<br />
/<br />
Fig.<br />
DETECTOR ARRAY<br />
6.4 A fiberoptic microbend brightfield electrical-bus-fed<br />
sensor array telemetry system.<br />
6-2<br />
ed to photodetectors in an array via fiberoptic cables.<br />
Some of the performance features of these and other<br />
fiberoptic sensor array configurations will now be<br />
discussed in some detail.<br />
An array of sensors may be used to beam-form<br />
or to signal average. In the former case it is necesaary<br />
to distinguish, i.e. maintain separation of, the<br />
output signals from the individual sensors. In the<br />
latter case the signals from a number of sensors are<br />
summed (OR-gated). For example, beam forming is used<br />
in echo ranging, while averaging can be used to discriminate<br />
between signals that arrive normal (perpendicular,<br />
transverse) to a linear array and those that<br />
arrive parallel (longitudinal) to the array. Thus,<br />
very often the spatial distribution of an array of<br />
fiberoptic sensors can be used to accomplish the multiplexing,<br />
mixing, or summing, of signals from the array.<br />
Although the principle of operation of only a linear<br />
array of sensors will be discussed, the same principles<br />
can be applied to multidimensional arrays.<br />
A linear array of fiberoptic sensors may be<br />
energized by means of a common bus. The bus may be an<br />
electrical conductor, fed by a direct-current power<br />
source or an alternating-current power source, or the<br />
bus may be an optical fiber fed by a relatively highpowered<br />
optical continuous-output source, such as a<br />
laser. Alternatively, in each of these situations, the<br />
power source output can be pulsed rather than be continuous,<br />
giving rise to four posaible arrangements,<br />
namely continuous electrical, continuous optical,<br />
pulsed electrical, and pulsed optical power. In any<br />
caae, the fiberoptic sensors (transducer, modulators)<br />
in the linear array may be either directly connected<br />
to the optical bus by means of a fiberoptic coupler,<br />
or a light source at each sensor may be connected to<br />
the electrical bus. The selection of the appropriate
method of sensor energization will depend on the power<br />
budget, risetime budget, distances to and within the<br />
array, and other matters related to the specific application.<br />
For the pulsed-bus method of energization of<br />
an equally-spaced linear array of sensors, spatial distribution<br />
of the sensors will cause the baaeband-modulated<br />
output signal pulse from each sensor of the array<br />
to occur at a different time according to the time it<br />
takes for a pulse to propagate from one sensor to an -<br />
other. If these signals are all fed into a single<br />
common return bus, they will be automatically timedivision<br />
multiplexed on that bus. This arrangement is<br />
shown in Fig. 6.6. Assume a pulse of light is dis-<br />
‘Warray = l/t = c(m - 1)/2nL (6.2) length of the array, c is the velocity of light in a<br />
For 50 sensors in a linear array, an optical<br />
fiber bus core refractive index of 1.5, a linear array<br />
500 meters long, Eq. (6.1) indicates that the time between<br />
the leading edges of array output pulses is:<br />
to=(2)( l.5)(500)/3(108) (49)=102 ns (6.3)<br />
The corresponding pulse repetition rate, PRR, is:<br />
PRR = l/t. = 1/102(10-9) = 9.8 kfPPS. (6.4)<br />
Thus, the input feed bus pulses cannot be<br />
wider than to. This is the rate at which the basebandsignal<br />
modulated pulses will emerge from the input-output<br />
end of the array. Also, some time should be allowed<br />
between pulses for random variations of sensor spacing,<br />
delays through sensor leads from and to the busses, and<br />
pulse risetimes. Therefore, the pulse length should<br />
not exceed 0.9to or about 90 ns for the above example.<br />
If they are wider, they are liable to overlap in the<br />
return bus. They can be narrower. The pulses will ar -<br />
rive as a train of pulses at the photodetector. The<br />
pulses in the train will come from and be in the same<br />
sequence as the sensors are positioned in the linear<br />
array. These events occur each time the feed bus is<br />
pulsed and as many pulses will be in each array output<br />
pulse train as there are sensors in the array. The<br />
photodetector must be capable of responding to about<br />
10 Mpps for the above example. If any analog-to-digital<br />
(A-D) conversion is to take place in a single A-D<br />
PHOTO– PULSED<br />
OETECTOR SOURCE<br />
converter fed by the return bus, the length of the<br />
pulses must be long enough to allow for analog to digital<br />
conversion. The repetition rate of the pulses in<br />
I r PULSED SOURCE OPTICAL FEEO BUSwlTH M. l<br />
LENGTHL~<br />
the train can be reduced by placing additional fiber<br />
)J LINEAR ARRAY between the sensors or by using a fiber with a higher<br />
refractive index, as indicated by Eq. (6.2).<br />
SPACEDINTENSITY-<br />
. . .<br />
MODULATION<br />
{r<br />
)J<br />
Various methods can be used to telemeter the<br />
sensor-modulated signals from the sensor array to a<br />
EQUALLY-SPACEO PULSES IN AN OPTICAL RETURN SUS<br />
photodetector. For example, the detector could be an<br />
A fiberoptic darkfield optical-bus-fed sensor<br />
array telemetry system with single op-<br />
is required, or the output of the photodetector could<br />
optical repeater if long distance optical transmission<br />
tical return bus.<br />
be transmitted electrically, via a wire line, coaxial<br />
cable, or radio-link. The radio frequency carrier<br />
could be modulated by the detected analog pulses or by<br />
A coupler at each sensor an analog-to-digital converter output. The above discussion<br />
applies each time a single light pulse is sent<br />
along the fiber bus. The maximum safe pulse duration<br />
was shown to be, from Eq. (6.1) and allowing a 10%<br />
The modulated pulse travels via the return bus safety margin:<br />
‘msx = 1.8nL/c(m - 1) (6.5)<br />
The maximum rate at which the pulses can be<br />
dispatched down the optical fiber feed bus is limited<br />
The distance between sensors is by the overall length of the array. Each pulse must<br />
travel twice the full length of the array and clear the<br />
The wave has to travel first sensor before the next pulse can be applied to<br />
the array. This maximum pulse rate is the maximum rate<br />
at which the baseband signal inputs to the fiberoptic<br />
aensors can be sampled. The minimum time between leading<br />
edges of feed bus pulses is twice the time length<br />
of the array, plus the pulse length (maximum possible<br />
The time pulse width is assumed) plus a safety margin for risetime<br />
and settling time. Therefore, these considerations<br />
the time between leading edges of output pulses<br />
will yield a minimum sampling period ts of:<br />
to=2[L/(m-1)] /(c/n)=2nL/c(m-1) (6.1)<br />
t+ = 2nL/c + 1.8nL/c(m - 1) + tr<br />
(6.6)<br />
ts = [2 + 1.8/(m - l)]nL/c + tr<br />
where m is the number of aenaors in the linear array, n<br />
is the refractive index of the fiber busses, L is the<br />
The physical parameter variation (baseband)<br />
to be sensed, such as a sound wave, a magnetic field<br />
variation, a pressure wave, or a force variation, will<br />
modulate the optical input to the fiberoptic sensor,<br />
thus producing an optical baseband-modulated signal output.<br />
This sensor output signal can be telemetered to a<br />
distant location (for detection and processing) in any<br />
of a number of different ways depending on spatial,<br />
timing, compositional, and other factors.<br />
Fig. 6.6<br />
patched along the feed bus.<br />
location taps a fraction of the light from the bus.<br />
The pulse of light enters each sensor in turn where it<br />
is modulated by the baseband signal imposed by the sensor.<br />
bsck to the photodetector for further processing. The<br />
minimum time that can be allowed for the spacing between<br />
the leading edges of pulses in the return bus is<br />
the propagation time between a given sensor location<br />
and the next sensor in the array and return to the given<br />
sensor location.<br />
L/(m - 1), where L is the length of the linear array<br />
and m is the number of sensors.<br />
the distance between aensors in the feed bus and in the<br />
return bus, therefore the travel distance is 2L/(m - 1).<br />
The speed of propagation of a lightwave in the bus is<br />
c/n, where c is the speed of light in a vacuum and n<br />
is the refractive index of the core. It iS assumed the<br />
refractive index is the same for both busses.<br />
of propagation is the distance divided by the speed,<br />
thus,<br />
is:<br />
The pulse repetition rate (PRR) of the pulses emanating<br />
from the linear senaor array is given by:<br />
6-3
vacuum, and t= is the overall risetime to be calculated<br />
later in this chapter. This value of ta can be reduced<br />
to the extent that the pulse width can be reduced.<br />
If there are only a few sensors in the array the<br />
second term in bracketa in Eq. (6.6) is significant.<br />
As the number of sensors is increased, the second term<br />
in Eq. (6.6) becomes less significant. Eq. (6.6) does<br />
not apply to one senaor because then L = O, the second<br />
term in brackets becomes indeterminate, and in fact<br />
there is no array. In this case, only the risetime<br />
requirement will place a limit on the sampling period.<br />
The maximum permissible sampling rate PR~s is:<br />
requirement for any specific spatial relationship among<br />
the sensors. The minimum sampling period for each sensor<br />
tssen in the array will be:<br />
‘asen<br />
= mtad (6.9)<br />
where m is the number of sensors in the array and tad<br />
is the analog-to-digital conversion time. This presumes<br />
a photodetector for each sensor output, a multiplexer<br />
(for polling each photodetector output), and a<br />
aingle A-D converter with its sample-and-hold and other<br />
associated circuitry aa shown in Fig. 6.8.<br />
Pluqs.= l/ts (6.7)<br />
where ts is defined in Eq. (6.6). The sampling rate<br />
can be arbitrarily reduced, but should not be less than<br />
twice the highest significant frequency component in<br />
the baseband signal in order to obtain reproduction of<br />
the baseband signal without significant distortion<br />
(Nyquist criterion).<br />
Another method for energizing an array of sensors<br />
is to connect the array to a pulsed electrical bus<br />
as shown in Fig. 6.7, rather than the pulsed optical<br />
>#<br />
I<br />
l--+-l<br />
EEk5?ltlzl<br />
‘1<br />
LENGTH L-~<br />
WLSSDELECTRICALF<br />
7’I w ,<br />
EWAUY-SPACEDPJSES NANOFTCAL REluRssus <strong>SENSOR</strong>S<br />
L-RARRAY<br />
OFMEWY<br />
SPACEDSENZORS<br />
WITNLSOAND<br />
INTSN.91v-M~L4T10N<br />
Fig. 6.8<br />
A fiberoptic star-coupler-fed sensor random<br />
array telemetry system with multiple and<br />
single cable returns.<br />
Fig. 6.7<br />
A fiberoptic lightfield pulsed<br />
bus-fed sensor array telemetry<br />
single optical return bus.<br />
electricalsystem<br />
with<br />
The random array of fiberoptic sensors may be<br />
energized instead by a direct-current electrical bus<br />
as shown in Fig. 6.9. In this case, there is a contin-<br />
bus just described. A light source, such as an LED, is<br />
optically connected to each sensor. Thia is the brightfield<br />
form of senaor energization. The return bus can<br />
be the same, as was shown in Fig. 6.6, and the analysis<br />
above still applies except that the propagation time<br />
in the electrical bus will be different. In this case,<br />
the electrical sampling pulae period will be:<br />
CONTFWOUS (DC) ELECTRICAL FEED BUS<br />
telec=l/2 [ts+[2+l.8/(m-l)]L/v+trc] (6.8)<br />
where the variables are as in Equation (6.6), v is the<br />
velocity of propagation in the electrical bus, and trc<br />
is the combined electrical and optical risetimes that<br />
will be discussed later in this chapter.<br />
Another configuration for energizing a randomly-distributed<br />
(non-linear) array of fiberoptic aensors<br />
is shown in Fig. 6.8. A continuous source of<br />
light (laser) energizes a star coupler that may be<br />
placed at the center of the array to reduce fiber requirements.<br />
The output of the coupler is fed to each<br />
fiberoptic sensor where it is modulated by the baseband<br />
signal. The senaor outputs are individually fed to an<br />
arrayof photodetector (PDs). In the arrangement<br />
shown in Fig. 6.8, the inputs to the photodetector (PD)<br />
array (one PD for each sensor) are time-division multiplexed,<br />
sampled, digitized, and telemetered as a digital<br />
data bit stream via a fiberoptic cable to another<br />
location for exploitation. In this case, there ia no<br />
6-4<br />
Fig. 6.9<br />
A fiberoptic electrical direct-current busfed<br />
sensor array telemetry aystem with<br />
multiple and single cable return.<br />
uous-output light source (LED) for each sensor. The<br />
baseband-modulated optical output of each sensor is<br />
separately cabled to a photodetector array and processed<br />
there in a manner similar to the preceding arrangement<br />
that had the continuous optical feed as was shown<br />
in Fig. 6.8.<br />
J
1<br />
The preceding discussion applied primarily to<br />
intensity-modulated lightfield and darkfield sensors.<br />
The outputs of arrays of other tYPes of sensors can<br />
also be telemetered to locations distant from the sensors.<br />
An interferometer sensor array configuration is<br />
shown in Fig. 6.10. The optical outputs of all fiber-<br />
(REPEAT OF<br />
R,G”T S,DE,<br />
Fig. 6.10<br />
OPTICAL BuS<br />
mL——...-.!<br />
\<br />
I<br />
COUPLERS<br />
ELECTROOPTIC PHOTODETECTORS<br />
INTEGRATED CHIP DETECTIONIFEEDBACK<br />
DIGITIZATION(MULTIPLEXER<br />
LED<br />
CLOCK<br />
L<br />
A fiberoptic interferometric star-couplerfed<br />
sensor array telemetry system with optical<br />
multiple cable and single cable return<br />
and integrated optical circuit chip.<br />
. . .<br />
There are many other variations and combinations<br />
of the basic fiberoptic sensor-array telemetry<br />
schemes shown here. The basic options include the<br />
selection of the type of telemetry link (to and from<br />
the sensor array, electrical, optical, or electrooptical);<br />
the type of fiber optic sensor (interferometric,<br />
intensity, phase, darkfield, brightfield); the type of<br />
coupling (star, tapped bus); the type of light sources<br />
(laser-powered or LED-powered bus, LED at each sensor);<br />
signal types (analog, discrete); multiplexing schemes;<br />
and many others. Each of these options will incur a<br />
different set of technical problems that require solution,<br />
a different set of costs, and a different set of<br />
performance characteristics. For example, frequencydivision<br />
multiplexing of fiberoptic sensor outputs can<br />
also be applied by energizing the common feed bus of<br />
the equally-spaced-sensor arrays discussed earlier with<br />
a constantly-changing-frequency pulse (frequency ramp).<br />
Thus, each fiberoptic sensor in the linear equallyspaced<br />
array will be fed a different frequency to be<br />
modulated by the baseband signal. The outputs can be<br />
demultiplexed with appropriate narrowband filters.<br />
6.1.3 Fiberoptic Sensor Array Budgets<br />
Fiberoptic aensor array budgets may be prepared<br />
in much the same manner as for the telemetry budgeta<br />
to be described in Subsection 6.2.3. Risetime,<br />
power, cost, and other budgets for fiberoptic sensor<br />
arrays depend on the same set of factors as for the<br />
entire sensor-telemetry system. tin optical power budget<br />
for the sensor array shown in Fig. 6.20 is as<br />
follows:<br />
optic sensors are brought to a common point, an electrooptic<br />
chip. The integrated optical chips are not<br />
yet commercially available, however, they are under<br />
development. A single optical fiber is used to conduct<br />
the output of the electrooptic chip to a distant location.<br />
Ml signal processing is done at the array location<br />
on the chip. The output of each senaor is sent<br />
to the single integrated fiberoptic chip for processing<br />
via a separate fiber. If It should prove desirable to<br />
use less fiber, use can be made of the spatial separation<br />
between sensors and the outputs can be automatically<br />
time-division multiplexed provided the signal processing<br />
can be accomplished at each interferometric<br />
sensor as ahown in Fig. 6.11. In this arrangement, a<br />
single optical return bus is used to telemeter the outputs<br />
to a distant location.<br />
T!+AE Owwm MULTIPLEXER<br />
Fig. 6.11<br />
0 ~-–<br />
LASER 1<br />
I<br />
REFEREW3EARM ‘<br />
II<br />
II<br />
POWER><br />
ELECTRCAL BUS :<br />
L--—-.——<br />
...__._J<br />
ELECTROOPTCCH!P<br />
Tlt.lEDIvISlON<br />
MULTIPLEXER<br />
A fiberoptic interferornetric star-couplerfed<br />
equally spaced sensor array telemetry<br />
system with electrical outputs to a single<br />
electrical return bus.<br />
6-5<br />
<strong>SENSOR</strong> ARRAY POWER BUDGET<br />
OUTPUT POWER<br />
Laser output power<br />
Coupling loas in fiber<br />
pigtail (78% Coupling)<br />
AVERAGE POWER OUTPUT<br />
SYSTEM LOSS<br />
Star coupler insertion loss<br />
Star coupler splitting loss (1:60)<br />
Coupler insertion loss (2, ldB each)<br />
3 dB coupler aplitting loss<br />
Fiber loss (300 m, 5 dB/km)<br />
Splicing loss (6, 0.5 dB each)<br />
TOTAL<br />
TOTAL<br />
POWEṚ<br />
6.2<br />
SYSTEM LOSS<br />
AVAILABLE MARGIN 37.3 - 29.3 =<br />
MARGIN AT EACH DETECTOR<br />
Antilog of 0.80 =<br />
<strong>FIBEROPTIC</strong> TELEMETRY SYSTEMS<br />
7 mW = 38.5 dB VW<br />
- 1.2 dB<br />
37.3 dB UW<br />
2.0 dB<br />
17.8<br />
2.0<br />
3.0<br />
1.5<br />
3.0<br />
29.3 dB<br />
8.0 dB VW<br />
6.3 UW<br />
The properties of optical fibers and fibersensors<br />
have been discussed in detail in prior<br />
optic<br />
chapters where particular attention was given to construction<br />
(materials and geometry), principles of operation<br />
(light transmission properties of fibers), and<br />
relative advantages of fiberoptic sensors over other<br />
types of sensors. Various ways were discussed in which<br />
fiberoptic sensors can be designed to measure absolute<br />
magnitudes or relative changes of a physical parameter,<br />
develop an output signal that is a function of these<br />
absolute or relative values, and emit this signal in a<br />
form suitable for subsequent processing and transmission.<br />
In essence, the fiberoptic aensor is a transducer;<br />
it provides the transform that enables an on-
site measurement of a physical parameter to be represented<br />
in a form (baseband signal) that can be directly<br />
and immediately processed and transmitted to another<br />
location, where it can be further processed and exploited<br />
for any desired use or application. Most, if<br />
not all, applications will require that the signal from<br />
a sensor be telemetered to a location other than the<br />
point of its generation. There are virtually no limits<br />
on the range of telemetering distances that may be required.<br />
llus, many fiberoptic sensors permit direct<br />
optical data transmission without conversion to electrical<br />
signals until photodetection. This section will<br />
be devoted to the configuration and use of fiberoptic<br />
sensor arrays, the telemetering of their outputs to<br />
other locations, and the reconversion of these signals<br />
to useful forms. Topics include system considerations,<br />
sensor systems, data transmission, data link analysis,<br />
repeater design, cable and connector design, and the<br />
budgeting of time, power and cost in telemetry systems.<br />
These topics may be summarized as:<br />
<strong>FIBEROPTIC</strong>:<br />
TELEMETRY SYSTEMS<br />
SYSTEN GENERAL CONSIDEIbiTIONS<br />
LINR ANALYSIS: RISETINE, POWER,<br />
AND COST BUDGETS<br />
<strong>SENSOR</strong> SYSTEMS<br />
REPEATER DESIGN<br />
CABLE AND CONNECTOR DESIGN<br />
END-TERMINAL RECEIVER CONSIDERATIONS<br />
The basic components of a telemetry system, from the<br />
sensors of the variations of a physical parameter to<br />
the instruments for displaying, recording, or simply<br />
using a representation of the variation at some destination<br />
user location are shown in Fig. 6.12.<br />
P<br />
?<br />
PHYSICAL<br />
PARAMETER<br />
0TRANSDUCER<br />
I<br />
El<br />
s-f(p)<br />
ENCODER<br />
MOOULATOR<br />
MULTIPLEXER<br />
CONVERTER<br />
TRANSMITTER<br />
SOURCE<br />
YEND INSTRUMENT<br />
DISPLAY<br />
SOUND<br />
RECORD<br />
COMPUTE<br />
E@<br />
TRANSMISSION<br />
I<br />
SINK<br />
Fig. 6.12 Basic components of a fiberoptic array<br />
telemetry system.<br />
6.2.2 Fiberoptic Telemetry System Basic<br />
Configurations<br />
Perhaps the most general telemetry system<br />
configuration is the multisource (sensor array), multiuser<br />
(user-array) general communication network-connected<br />
system shown in Fig. 6.13. The simplest system<br />
ARRAY<br />
SOURCE<br />
<strong>FIBEROPTIC</strong><br />
CABLES<br />
1<br />
m------<br />
Fig. 6.13<br />
<strong>FIBEROPTIC</strong>, RADIO,<br />
OR WIRE<br />
L<br />
TRANS-<br />
MISSION<br />
SYSTEM<br />
-----El .<br />
---b<br />
Generalized fiberoptic telemetry system.<br />
is a single sensor connected to a single output device<br />
via a single channel. Many variations are poasible,<br />
for example the multisource, multiplexed, single user,<br />
fiberoptic data link configuration shown in Fig. 6.14.<br />
El-<br />
1<br />
<strong>FIBEROPTIC</strong><br />
CABLES<br />
SIGNAL<br />
CONDl-<br />
4 TIONER<br />
I 1’<br />
. . .<br />
‘B-J<br />
5<br />
ṅ<br />
Fig. 6.14<br />
FOCABLE<br />
USER END INSTRUMENTS<br />
RECORDER<br />
DISPLAY DEVICE<br />
LOUDSPEAKER<br />
COMPUTER<br />
TRANSMITTER<br />
0<br />
photodetector<br />
AND DEMUX<br />
A multisource multiplexed single-uaer fiberoptic<br />
sensor array telemetry system.<br />
6.2.1 Fiberoptic Telemetry System Design OptiOnS<br />
Mny options are open to the designer of a<br />
fiberoptic telemetry system. These include the determination<br />
of the overall system configuration; the design<br />
and selection of fiberoptic senaors, cables, and<br />
connectors; the design and selection of transmitters<br />
and receivers; and the specification of system parameters,<br />
such as signal-to-noise ratios, distortion<br />
limits, permissible bit error-rates, multiplexing<br />
schemes, modulation methods, and the coding, sensing,<br />
and detection arrangements.<br />
6-6<br />
Various arrangements for the transmission of<br />
signals from a fiberoptic sensor array to many users<br />
via different types of fiberoptic data links are ahown<br />
in Fig. 6.15. The simplex, half-duplex, full-duplex,<br />
and multiplex schemes illustrated in Fig. 6.15 describe<br />
various system configurations with different capabilities.<br />
These configurations may be connected to operate<br />
as one-way-at-a-time, two-way alternate, or two-way<br />
simultaneous systems. For example, two simplex channels<br />
could be associated for operating a two-way simultaneous<br />
data link.
SIMPLEX <strong>FIBEROPTIC</strong> TRANSMITTER <strong>FIBEROPTIC</strong> RECEIVER<br />
I<br />
%T21<br />
<strong>FIBEROPTIC</strong> SPLICE<br />
I<br />
G<br />
DUPLEX<br />
T,<br />
cl-l<br />
w —<br />
R2<br />
m RI<br />
m T2<br />
3+! -’,<br />
‘\ \’<br />
<strong>FIBEROPTIC</strong> CONNECTOR<br />
<strong>FIBEROPTIC</strong> CABiE<br />
Fig. 6.16<br />
A fiberoptic data link.<br />
m 4’ E<br />
‘“’’’’”x Km7dl<br />
Fig. 6.15<br />
6.2.3 Telemetry System Budgets<br />
Generalized transmission schemes.<br />
Each telemetry system component interacts<br />
with other components within many time and space constraints.<br />
This gives rise to many different ways of<br />
aPPIYing the constraints. Each component may provide<br />
useful power, consume available power, occupy limited<br />
space, contribute to overall weight, poasesa a useful<br />
life, require maintenance, has an acquisition and connection<br />
cost, or has other features that affect the<br />
whole system. Thus, each component makes a contribution<br />
to, or imposes a liability on, the whole system<br />
in each of these areas. If there are limits to resources<br />
or characteristics that are imposed on the<br />
whole system, there will be a requirement to budget<br />
them. h obvious example is to place a limit on system<br />
cost, space, and weight and then aelect a aet of components<br />
whose total cost, space, and weight do not<br />
exceed theae limits. Budgeting of time, power, and cost<br />
will be discussed for fiberoptic telemetry systems.<br />
6.2.3.1 Rise Time Budget Analysis<br />
Distortion, length of lines, attenuation,<br />
signaling (pulse-repetition) rates, and dispersion will<br />
place a limit on the length of time that can be allowed<br />
for a step or pulse input to a fiberoptic transmitter<br />
to reach the 90% of maximum signal level at the output<br />
terminal of the receiver. This risetime is distributed<br />
over the electrical and optical serially-connected<br />
(tandem connected) components of the link on the basis<br />
of an approximated Gaussian “distribution in which the<br />
combined risetime of the components in tandem is the<br />
square root of the sum of the squares (RMS) of all the<br />
risetimes of the serially-connected components. Normally<br />
the total link risetime is the root-meansquare of<br />
the transmitter, cable, and receiver risetimes. However,<br />
these components themselves may have serial<br />
elements each with individual risetimes. For example,<br />
the transmitter may have an electronic risetime and a<br />
fiberoptic pigtail and coupler risetime. The cable<br />
may have splices or repeaters. All the risetimes of<br />
these are combined on the same RMS basis. A schematic<br />
diagram of a simple fiberoptic link ia shown in Fig.<br />
6.16. The elements that comprise the risetime of the<br />
fiberoptic link are as follows:<br />
TRANSMITTER RISETIME, tr(xmtr., primarily due to the<br />
—————<br />
the light source and driver e ectronics.<br />
———<br />
FIBER RISETI~-, tr(cable), due to the modal dispersion<br />
(variation in group delay between fiber modes)<br />
and .— material dispersion (nonlinear variation of the<br />
refractive index, or as a function of wavelength).<br />
Modal dispersion in an optical fiber is a<br />
combination of —-— intramodal — dia~ersion and intermodal<br />
dispersion. Intramodal ~ is pulse broadening<br />
in an optical fiber. It is primarily a function of<br />
the spectral bandwidth of the source and the material<br />
dispersion, to be discussed later. The intramodal<br />
dispersion, Sintram, of an optical fiber is given by:<br />
s intram<br />
= (SAL/c)d2n/d21 (6.10)<br />
where S = Spectral bandwidth of source<br />
k = Wavelength of source, midband<br />
L = Length of fiber<br />
= Speed of light in a vacuum<br />
d2n/di~ = Material dispersion, in which n is the core<br />
refractive index and 1 is the source wavelength<br />
The only deaign option for reducing intramodal dispersion<br />
at a given source wavelength and length of fiber<br />
is to reduce the source spectral bandwidth. The spectral<br />
bandwidth of a typical LED is of the order of<br />
0.05 Vm whereaa that of a typical laser is 0.002 pm.<br />
Intermodal dispersion is pulse broadening due<br />
to differences in propagation velocity, and hence propagation<br />
time, among the various modes. Proper shaping<br />
of the refractive index profile of an optical fiber<br />
can reduce intermodal dispersion to a minimum. Intermodal<br />
dispersion, Sinterm, is given by:<br />
Sintem = (LnA/2c)pi (6.11)<br />
where L = Length of fiber<br />
n = Refractive index at center of fiber<br />
A = (nl-n2)/nl, where nl and n2 are the maximum<br />
and minimum refractive indices , respectively.<br />
It is called the index difference parameter<br />
c = Speed of light in a vacuum<br />
p i<br />
= Refractive index profile parameter, ideally<br />
equal to 2.25, based on zero intermodal dispersion<br />
The individual contributions to dispersion within modes<br />
and among modes in a given optical fiber follow a Gaussian<br />
distribution. Therefore, if Eq. (6.10) and (6.11)<br />
are squared, added, and the length, L, factored, and<br />
the square root of the sum of the squares is taken, the<br />
6-7
following is obtained:<br />
L-BWP= [(SX/c)d2n/dA2]2+[(nA/*c)pi]2<br />
[ 1 1’2 (6.12)<br />
where L-BWP is the optical fiber length-bandwidth product.<br />
Many of theae parameters are fixed by the optical<br />
fiber manufacturer. In addition, the modal dispersion<br />
caused by a fiber can be expressed in terms of the<br />
risetime for a step input optical signal. This can be<br />
empirically determined for typical high performance<br />
commercially available optical fiber. The parameters<br />
given in Eqa. (6.10) and (6.11), and therefore (6.12),<br />
contribute to the fiber riaetime modal dispersion coefficient<br />
used in Eq. (6.13) below.<br />
The portion of the fiber risetime due to<br />
modal dispersion (intramodal and intermodal) ia given<br />
empirically for a typical high-performance commercially<br />
available optical fiber, as:<br />
where L-BWPO =<br />
FIBER RISETIME DUE TO MODAL DISPERSION<br />
L-BWP =<br />
L eff =<br />
where L=<br />
530 =<br />
trmo(cable) = 530/L-BWpo ‘s (6.13)<br />
(L-Bwp)/Leff = Optical 3-dB bandwidth of<br />
the fiber.<br />
Length-bandwidth product, MRz-km.<br />
L x = Effective length of fiber.<br />
Actual length of fiber.<br />
0.5 < x < 1<br />
Short lengtha, < 1 km, x = 1<br />
Long lengths, x = 0.7 or 0.8.<br />
Fiber risetime modal dispersion coefficient<br />
for typical high-performance commercially<br />
available optical fiber.<br />
The portion of the fiber risetime due to<br />
material dispersion is given aa:<br />
where<br />
FIBER RISETIME DUE TO MATERIAL DISPERSION<br />
‘rma(cable) = 1.1 MSL (6.14)<br />
M = Material dispersion coefficient, given<br />
in nslnm-km and as shown in Fig. 6.17.<br />
S = Spectral bandwidth of source, nm<br />
L = Link length, km<br />
A typical curve for the value of M, the material<br />
dispersion coefficient, as a function of wavelength<br />
for two specific glasses is shown in Fig. 6.17.<br />
RECEIVER RISETIME, tr(rcvr), due to the photodetector<br />
and its aaaociated electrical circuits. The<br />
receiver risetime la normally given by the manufacturer<br />
or can be constructed or eatimated from<br />
the manufacturer’s data.<br />
Normally a Gauasian distribution of the risetimes<br />
is assumed, and thus for a set of sequential<br />
components the overall risetime for the system is<br />
given as:<br />
‘r(sya) = [t2*(xmtr) +<br />
2<br />
‘r ma(cable) + ‘r(rcvr)<br />
2<br />
r mo(cable) +<br />
1/2<br />
(6.15)<br />
However, the total risetime for the link,<br />
‘r(sys)~ cannot exceed the maximum allowable risetime<br />
for the link. In digital systems, the allowable risetime<br />
is limited by the requirement to prevent the bit<br />
error rate (BER) due to interaymbol (interpulse) interference<br />
from exceeding a prescribed value. In analog<br />
systems the frequency response at high frequencies must<br />
be sufficient to prevent distortion of the base band<br />
aignals. For example, in the nonreturn-to-zero (NRZ)<br />
method of signal representation (code), ‘he ‘r(sys)<br />
must be less than 0.7 times the bit interval, expressed<br />
as the reciprocal of the bit rate. If the bit rate<br />
ia 7.0 Mb/see, the maximum value tr(sys) can have ia<br />
is 100 nsec for NRZ coding. For return-to-zero (RZ)<br />
coding the factor is 0.5, in which case, for the same<br />
bit rate of 7.0 Mb/see, the maximum allowable tr(sya)<br />
is 71.4 ns.<br />
The following is given as an example of a<br />
riaetime budget for a typical fiberoptic link:<br />
LINR<br />
DESCRIPTION<br />
<strong>FIBEROPTIC</strong> LINK RISETIME BUDGET<br />
Data rate, Rw<br />
Link length, L<br />
Length-bandwidth-product, L-BWF<br />
Light source<br />
Operating wavelength,a<br />
Light source spectral width, S<br />
COMPONENT RISETIMES<br />
Transmitter [tr(xmtr)] (Manufacturer) *O ns<br />
Fiber modal dispersion risetime [trmo(cable)]<br />
7.0 Mb/see<br />
1.5 km<br />
50 MHz-km<br />
LED<br />
0.830 Pm<br />
0.020 pm<br />
0.25<br />
(L-BWo) =<br />
(L-BWP)/Lx = 50/1.5°”8 = 36.1 MRz-km<br />
015<br />
010<br />
‘rmo(cable)<br />
= 530/(L-BWPo) = 530/36.1 = 14.7 ns<br />
Fiber material dispersion risetime<br />
M = 75 ns/m-km (Manufacturer)<br />
[t_(cable)]<br />
‘rma(cable)=l- lMsL=( 101)(75)(0”02)(1-5)=2”5ns<br />
Receiver risetime [tr(rcvr)] (Manufacturer)<br />
0.05<br />
0<br />
/00 900 1100 1: )<br />
WAVELENGTH(nm)<br />
Fig. 6.17 The material dispersion coefficient versus<br />
wavelength for two types of glasses.<br />
6-8<br />
‘r(rcvr)<br />
LINR RISETIME<br />
= 375/Belec = 375/50 = 7.5 ns 56.3<br />
Substituting the above risetimes in Eq. (6.15) the<br />
overall system (link) risetime is calculated to be<br />
26 ns.
MAXIMUM ALLOWABLE RISETIME = 0.7/RN~ = 100 nS <strong>FIBEROPTIC</strong> LINR OPTICAL POWER BUDGET<br />
(Fig. 6.16)<br />
RISETIME BUD(ZT MARGIN = 7fI ns<br />
LINK DESCRIPTION<br />
The 74 ns margin between the maximum allowable<br />
risetime based on the required signaling rate and<br />
Link length, L<br />
1.5km<br />
Data Rate, R<br />
7.0 Mblsec<br />
the system risetime for all the components can be used<br />
Operating wavelength<br />
0.830 nm<br />
in many ways. For example, the cable could be made<br />
longer, the signaling rate could be increased, or a<br />
cheaper cable with a greater material or modal dispersion<br />
per unit length could be used. However, other<br />
budgets, such as the power budget, may place limits on<br />
theae changes. Perhaps the one single fact to remember<br />
in regard to risetime is that it represents reciprocal<br />
dollars, i.e., the longer the risetime, the cheaper<br />
the component. Therefore, except for a power safety<br />
margin, all allowable risetime should be used up for<br />
the performance requirement in a given application.<br />
6.2.3.2 Optical Power Budget Analysis<br />
The optical power requirement of a given<br />
fiberoptic telemetry system is also a matter of distribution<br />
of power over a serial or a parallel set of<br />
fiberoptic channels. For example, if there are star<br />
couplers, there must be sufficient input power to satisfy<br />
the input power requirement for each parallel output<br />
channel. Serially connected components, such as<br />
cables, splices, and couplers, will each have an inser -<br />
tion loss. Repeaters will insert a gain. The losses<br />
and gains are added to obtain the source-to-receiver<br />
overall loss. The optical power dissipation that can<br />
be allowed is the difference between the sum of the<br />
transmitter and repeater optical power outputs and the<br />
required receiver (photodetector) optical power input<br />
in order to keep the bit error rate (BER) below, or<br />
signal-to-noise ratio (S/N) above, a specified value.<br />
A typical allowable optical power loss between transmitter<br />
and receiver for various data rates at an allowable<br />
BER of 10-9 is shown in Fig. 6.18. Normally one<br />
TRANSMITTER POWER, pT<br />
Light source type<br />
Average source optical power<br />
Fiber coupling loss<br />
Average launched optical power,<br />
REQUIRED RECEIVER POWRR, pREQ<br />
Detector type<br />
Required bit error rate, BER<br />
Receiver bandwidth<br />
Receiver sensitivity<br />
Link margin<br />
‘REQ<br />
ALLOWABLE LINK LOSS OVER MARGIN, PAL<br />
pm = PT - PmQ = -14 -(-48) = 34 dB<br />
LINR LOSS COMPUTATION<br />
LED 0.1 mW<br />
-10 dBm<br />
-4 dB<br />
-14 dBm<br />
PIN-FET<br />
1(3-9<br />
50 MHz<br />
-55 dBm<br />
+ 7 dB<br />
-48 dllm<br />
Contributor Unit Quantity Total<br />
Recr coupling 3.0 dB 1 3.0 dB<br />
Connectors 2.0 2 4.0<br />
Splices 0.5 4 2.0<br />
Cable 5.0 dB/km 1.5 km 7.5<br />
Splitters<br />
Margin 2.0 dB 2.0<br />
Total link loss<br />
18.5 dB<br />
REMAINING POWER MARGIN<br />
(Allowable - Total link loss) = 34- 18.5<br />
= 15.5 dB<br />
=<br />
II<br />
g<br />
n<br />
Fig. 6.18<br />
o<br />
-lo<br />
-20<br />
-30<br />
-40<br />
-50<br />
-60<br />
-70<br />
t<br />
LASER-LAUNCHED<br />
POWER RANGE<br />
LED-LAUNCHED<br />
--..POWER RANGE _______ -14<br />
I<br />
-80<br />
-901 1 1 1<br />
1 10 100 1000<br />
DATA RATE (Mb/s)<br />
BER =10-9<br />
optical power loss versus data rates for<br />
the fiberoptic data link used in the optical<br />
power budget analysis in Section 6.1.3.<br />
would not use up all the available power, but maintain<br />
a safety margin of a few dB to insure satisfactory performance.<br />
The allowable loss is then distributed over<br />
the fiberoptic link components as shown in Fig. 6.16<br />
and given in the following example:<br />
Since a link margin of 7 dB and a link loss<br />
computation margin of 2 dB have already been allowed,<br />
the entire 34 dB may be used up. The loss in the link<br />
of the given design is 18.5 dB. Therefore, there is an<br />
excess total available optical power margin of 15.5 dB.<br />
It may be cheaper to use up this excess margin by<br />
selecting cheaper cable components with greater losses<br />
or it may be cheaper to choose a lower-power source.<br />
Link power is like dollars, it is best to get by with<br />
the least power, low power sources being cheaper. However,<br />
link loss is more like reciprocal dollars, the<br />
greater the power loss, the cheaper the components.<br />
Therefore, there is a trade-off to be made in order to<br />
minimize the overall cost of a fiberoptic link.<br />
6.2.3.3 Cost Budget Analysis<br />
The cost of a fiberoptic telemetry system<br />
will be based on judicious maximal use of available<br />
risetime and minimal use of power as well as many other<br />
factors. Fiberoptic cable designs, repeater spacing,<br />
multiplexing schemes, allowable BERs, cable routings,<br />
the use of overhead versus subterranean cables, availability<br />
of components, simplicity of design and fabrication,<br />
and ease of maintenance, are just a few of the<br />
many factors that will enter into the overall cost of<br />
the system.<br />
6.2.4 Fiberoptic Telemetry System Specific<br />
Configurations<br />
An example of a set of the final design para-<br />
6-9
meters for the field tested fiberoptic long-haul telemetry<br />
system shown in Fig. 6.19 is as follows:<br />
LONG HAUL <strong>FIBEROPTIC</strong> LINR PERFORMANCE DATA<br />
PROCESSING STATION TRANSMISSION PARALLEL <strong>SENSOR</strong> ARRAY<br />
LINK<br />
,—<br />
SYSTEM LENGTH<br />
REPEATER SPACING<br />
NUMBER OF REPEATERS<br />
Diameter<br />
Length<br />
Weight<br />
OPEIUiTING DEPTH<br />
CABLE DIAMETER<br />
CABLE STRENGTH<br />
DATA FORMAT<br />
FULL DUPLEX<br />
WAVELENGTHS<br />
HIGH BIT RATE CHANNEL<br />
Bit Error Rate (BER)<br />
Low Bit Rate<br />
Bit Error Rate (BER)<br />
70 km<br />
6.8 to 8 km<br />
8<br />
2.9 cm<br />
30.5 cm<br />
< 400 g<br />
1000 m<br />
2.4mm<br />
60 kg (0.8% Strain)<br />
Digital PCM<br />
1 Fiber<br />
0.83 and 1.06 pm<br />
22 Mb/s<br />
< 10-9<br />
43 kb/s<br />
< 10-7<br />
2+<br />
DEMODU-<br />
LATOR<br />
SIGNAL<br />
PROCESSOR<br />
DISPLAY<br />
i<br />
LASER<br />
OR LED \<br />
: <strong>FIBEROPTIC</strong><br />
RECEIVER<br />
t-1<br />
PHOTODETECTOR [<br />
CONNECTOR<br />
Fig. 6.20 An example of a fiberoptic sensor array<br />
multimode intensity modulated telemetry<br />
system.<br />
h<br />
The above system is the Naval Ocean Systems<br />
Center and the International Telephone and Telegraph<br />
(NOSC/ITT) Undersea Single Fiber Multirepeater Full<br />
Duplex Electrooptical Data Link, a schematic diagram of<br />
which was shown in Fig. 6.19.<br />
PROCESSING STATION TRANSMISSION LINEAR<strong>SENSOR</strong> ARRAY<br />
LINK<br />
HBR RCVR<br />
LBRXMTR<br />
)<br />
_HBR(22 MBISEC)<br />
LBR (43KBISEC)C<br />
SPACING: 8km BTWN REPEATERS<br />
Al= .83pm LASER<br />
A2=106#mLED<br />
<strong>SENSOR</strong><br />
STRING<br />
liBRXMTR<br />
LBRRCVR<br />
EOREP1<br />
LBR<br />
I I<br />
liBR<br />
EOREP2<br />
-<br />
HBR(A1) ~ EOREP8<br />
_LBR(A2)<br />
I<br />
1<br />
1<br />
,<br />
t<br />
[.<br />
DEMODU<br />
LATOR<br />
SIGNAL<br />
PROCESSOR<br />
DISPLAY<br />
8<br />
Fig. 6.21<br />
q J J 1<br />
: FIBER<br />
; COUPLERS<br />
AII example of a fiberoptic sensor array<br />
multimode intensity modulated telemetry<br />
system.<br />
Fig. 6.19<br />
The Naval Oceans Systems Center and the International<br />
Telephone and Telegraph (NOSC/<br />
ITT) undersea single fiber multirePeater<br />
full duplex electrooptical data link.<br />
There probably is no limit to the number of<br />
different fiberoptic sensor array system configurations<br />
that can be designed, considering the number of energization<br />
methods, types of sensors, and return telemetry<br />
methods that can be uaed. Four specific fiberoptic<br />
telemetry system and sensor array configurations are<br />
shown in Figs. 6.20 through 6.23. Specific design<br />
aspects of basic configurations will be discussed in<br />
following subsections.<br />
PROCESSING<br />
STATION<br />
c=<br />
TIMING<br />
D<br />
FIBEROPTC<br />
RECEIVER<br />
cl<br />
DEMOCY.JLATOR<br />
aSIGNAL<br />
PROCESSOR<br />
DSPLAY<br />
I<br />
TRANSMISSION<br />
LINK<br />
ELECTRICAL FOWER<br />
-<br />
<strong>FIBEROPTIC</strong> CASLE<br />
I<br />
ARRAY<br />
Fig. 6.22 An example of a fiberoptic interferornetric<br />
sensor array telemetry system.<br />
6-10
PROCESSING STATION TRANSMISSION wAVELENGTHM ULTIPLEXED<br />
LINK<br />
ARRAY<br />
BDEMODU-<br />
LATOR<br />
SfGNAL<br />
PROCESSOR<br />
c1<br />
OISPLAY<br />
[<br />
i<br />
BROAD<br />
s:::~::M<br />
RECEIVER<br />
IQ<br />
<strong>FIBEROPTIC</strong><br />
CONNECTOR<br />
Ld<br />
;DIFFRACTION<br />
: GRATING<br />
; ~A’&<br />
Fig. 6.23 An example of a fiberoptic diffraction<br />
grating senaor array telemetry system.<br />
n<br />
For m parallel channels with equal pulse intervals,<br />
this reduces to:<br />
RE = (m/T) log2 n. (6.17)<br />
For two condition modulation, this reduces to m/T.<br />
For a single channel, RT reduces to (l/T) log2n,<br />
and with 2 conditions, I/T, i.e., the baud rate<br />
for one channel. Each of the multiplexed fiberoptic<br />
channels can be used as an analog (voice,<br />
sound, continuous signal) or as a digital (pulse<br />
coded) channel.<br />
6.3.2 Transmission Line Specific Parameters<br />
The construction features of a fiberoptic or<br />
electrooptic transmission line (cable) depend on many<br />
environmental factors. Some of these are as follows:<br />
6.3 <strong>FIBEROPTIC</strong> <strong>SENSOR</strong> ARRAY TELEMETRY TRANSMIS-<br />
SION LINE PARAMETERS<br />
6.3.1 Transmission Line General Parameters<br />
Fiberoptic array data transmission line designs<br />
include a large but manageable number of options<br />
and variables. A few of these are as follows:<br />
GENERAL <strong>FIBEROPTIC</strong> TRANSMISSION LINE DESIGN PARAMETERS<br />
SIGNAL MODE<br />
Analog, digital, hybrid, discrete<br />
MODULATION SCHEME<br />
Phase, frequency, intensity, polarization, wave -<br />
length<br />
CHANNEL CAPABILITY<br />
Simplex, duplex, half-duplex, diplex, multiPlex<br />
OPERATIONAL MODE<br />
One way, one way at a time, two way simultaneous<br />
CABLE DESIGN<br />
Fibers, strength members, conductors, jacket,<br />
filling, insulation, buffering, spacing type,<br />
spacing<br />
FAIL-SAFE<br />
Redundancy, power margin, tolerance to breaks<br />
ATTENUATION<br />
Absorption, scattering, insertion loss, bit error<br />
rate (BER)<br />
DISPERSION<br />
Bit error rate (BER), distortion, signal-noise<br />
ratio<br />
RELIABILITY<br />
Failure rates, failure modes<br />
OVERALL CHANNEL SIGNALING RATE<br />
In digital systems the number of transmission<br />
lines or channels will be determined by the total<br />
data signaling rate requirements and the multiplexing<br />
schemes that are used. For example, assume<br />
many channels with different signaling rates and<br />
different digital pulsing schemes connect two stations.<br />
Then, the total data aignaling rate (capacity<br />
between the stations, or as an output capacity<br />
from one to many stations) for a group of m parallel<br />
channels in which Ti is the minimum interval<br />
in seconds between signal transitions for the i-th<br />
channel and ni is the number of significant conditions<br />
of modulation, is given by:<br />
m<br />
RT = ~ (1/Ti) log2 ni (6.16)<br />
1=1<br />
6-11<br />
<strong>FIBEROPTIC</strong> CABLE DESIGN PAMMETERS AND<br />
ENVIRONMENTAL FACTORS<br />
PHYSICAL STRENGTH PARAMETERS<br />
Tensile Strength<br />
Radial Compression Strength<br />
Flex Resistance<br />
Bend Resistance<br />
Abrasion Resistance<br />
Vibration Resistance<br />
Strength Member Location<br />
Strength Member Materials<br />
ENVIRONMENTAL FACTORS<br />
Operating Temperature<br />
Operating Pressure<br />
Moisture/Chemical/Other Resistance<br />
OPTICAL FIBER PARAMETERS<br />
Multimode or Single Mode<br />
Glass or Plastic<br />
Refractive Index Profile<br />
Core Concentricity<br />
Cladding Outer Diameter<br />
Numerical Aperture<br />
Fiber Jacket Material<br />
Fiber Jacket Thickness<br />
Dispersion (Modal and Material Multimode<br />
vs Singlemode)<br />
Attenuation Per Unit Length<br />
Lose and Bandwidth Stability<br />
Costings on Fibers<br />
Number of Fibers<br />
Ease of Joining<br />
Size of Fibers<br />
CABLE PARAMETERS<br />
Size of Cable<br />
Bend Radii<br />
Sheathing<br />
Location of Fibers<br />
Armor Requirements<br />
ELECTRICAL FEATURES<br />
Electrical Heating<br />
Wire Size<br />
Number of Conductors<br />
Shielding<br />
h example of an electrooptic cable crosssection<br />
is shown in Fig. 6.24. The need for built-in-
55/125 pm, F.4uI-TIMODE,<br />
Gl, OPTICAL FIBER \<br />
EL BUFFER TO<br />
D. OF 1.02 mm<br />
‘r<br />
4<br />
15 CU-CLAD-STEE<br />
WIRES – EACH 0.<br />
0. D. – AS HELIX<br />
;KET TO 2.54 mm<br />
Fig . 6.24 A cross section of one of a large number of<br />
different electrooptic cable designs.<br />
cable fiberoptic repeaters is determined by the risetime<br />
and power budgets, which in turn, depend on attenuation<br />
and cable length-between-repeaters. An example<br />
of a fiberoptic electrooptic repeater is shown in Fig.<br />
6.25. This repeater handles a high bit-rate in one di-<br />
24<br />
Fig. 6.27<br />
~<br />
01 1000<br />
FREQUENCY (MHz)<br />
The optical power loss per hertz for one<br />
kilometer lengtha of several types of cables<br />
at various frequencies.<br />
6.3.3 Multiplexing with Optical Fibers<br />
Multiplexing may be accomplished with optical<br />
fibers in the following ways:<br />
HBR(A,)<br />
TOPROCESSING— OPTCAL<br />
— STATION — DuPLEXER<br />
Fig. 6.25<br />
+=+<br />
LSR(A2)<br />
OPTICAL<br />
DU~ER —<br />
LSR<br />
H=?HSR<br />
OTHER REKATERS<br />
h example of a fiberoptic full duplex repeater.<br />
rection for user data and a low bit-rate in the other<br />
direction for control and supervisory data in a single<br />
fiberoptic cable. An arrangement for the optical duplexers<br />
that was shown in Fig. 6.25 is sho~ in Fig.<br />
6.26.<br />
FREQUENCY -DIVISION MULTIPLEXING (FDM)<br />
Modulate a single optical wavelength with a different<br />
carrier frequency for each channel.<br />
WAVELENGTH-DIVISION MULTIPLEXING (WDM)<br />
Use two or more optical sources each with a different<br />
wavelength for each channel.<br />
TIME-DIVISION MULTIPLEXING (TDM)<br />
Different time-slot for each channel.<br />
sPAcE-DIvxsIoN MULTIPLEXING (fiDM)<br />
Different fiber for each channel.<br />
POLARIZATION<br />
Different form of polarization for each channel.<br />
The multiplexing scheme that is used for a<br />
given application depends on the number of channels required<br />
and the cost factors for each scheme. A typical<br />
multiplexing arrangement is shown in Fig. 6.28. In<br />
TOHSR<br />
RCVR<br />
Fig. 6.26<br />
. . ()<br />
. ---<br />
_HSR<br />
6 Q A, .<br />
_LSR<br />
A2 Q<br />
‘<br />
----<br />
~.<br />
p<br />
AZFROM<br />
--- LSRXMTR<br />
‘- ‘- ““-~%1:<br />
DICHROIC<br />
FILTER<br />
An arrangement for a fiberoptic duplexer.<br />
m<br />
2<br />
1<br />
$<br />
Fig. 6.28<br />
<strong>SENSOR</strong><br />
ARRAY<br />
TRANSMl~ER<br />
IJULILS,GNAL / \ ( /<br />
-’45-J ‘RECE’VER<br />
AQQ.. nlln<br />
An example of a fiberoptic sensor lineararray<br />
telemetry system with single optical<br />
repeatered cable return.<br />
tin indication of the power-loss-per-hertz<br />
versus frequency for an optical fiber, compared to wire<br />
pairs and coaxial cables, iS sbo~ in Fig. 6.27. Note<br />
that in the graded-index fiber the loss-per-hertz is<br />
almost independent of frequency for frequencies up to<br />
almost one gigahertz.<br />
this figure, the signals from the sensor array are<br />
multiplexed on a time-division multiplexing (TDM) basis<br />
so that only one series of repeaters is required for a<br />
single fiber. This basic fiberoptic link consists of<br />
a fiberoptic transmitter (modulated light source), a<br />
6-12
fiberoptic cable (optical cable), and a fiberoptic<br />
receiver (photodetector). Electrical-to-optical and<br />
optical-to-electrical conversion (transduction) is presumed<br />
at each end, though such presumption is not always<br />
true for all fiberoptic links. For example, the<br />
receiving end may consist of a fiberscope (display device)<br />
or simply a flashing light indicator of on-off<br />
conditions.<br />
6.3.4 Connector Parameters<br />
There are many performance requirements and<br />
design considerations that enter into the choice of<br />
suitable connectors for fiberoptic cables. In addition<br />
to the optical insertion loss introduced by the connector,<br />
other optical features such as axial misalignment,<br />
axial offset, and spacing between fibers must be considered,<br />
as was indicated in Chapter 3. Some of the<br />
connector physical features and design considerations<br />
are as follows:<br />
After a physical parameter, such as a sound<br />
wave or a varying magnetic field, has been sensed and<br />
transformed by a fiberoptic sensor into modulated light<br />
that is then transmitted to a point of use via a fiberoptic<br />
telemetry system, the modulated light has to be<br />
demodulated in order to recover the information-bearing<br />
signal. One or more photodetectors may be required to<br />
obtain an electrical signal that may be used as is or<br />
further processed by electrical circuits. Demultiplexing<br />
may be required to obtain the separate signals that<br />
were originally generated or transmitted. For digital<br />
data, decoding will be necessary to convert the pulse<br />
codes to analog form or to recover alphanumeric data.<br />
In some cases, the incoming signals need not be converted<br />
to electrical signals, but ULSY be directly displayed<br />
as light signals, such as for signaling on-off<br />
conditions or for telemetering images received via a<br />
multifiber coherent optical cable connected directly<br />
to the faceplate of a fiberscope. Thus, the type of<br />
processing that must be performed on incoming lightwave<br />
signals at an end terminal depends on the specific<br />
application.<br />
6.5 SUMMARY<br />
The topics that were covered in this chapter<br />
included fiberoptic telemetry system configuration;<br />
system risetime, power and cost budgeting; sensor array<br />
design and construction; and fiberoptic transmission<br />
considerations, including multiplexing and fiberoptic<br />
cable, repeater, and connector design considerations.<br />
CONNECTOR DESIGN CONSIDERATIONS<br />
NUMEER OF ELECTRICAL LEADS AND SIZE<br />
NUMBER OF OPTICAL FIBERS AND SIZE<br />
OPERATING TEMFERiTURR AND PHESSURE<br />
MOISTURE AND DIRT RESISTANCE<br />
FIELD MATABILITY<br />
STRAIN RELIEF DESIGN<br />
An example of a ruggedized connector is shown<br />
in Fig. 6.29.<br />
ACHlEVED2.8dS LOSS WHEN COUPLING<br />
50#m CORE0.2 NAGRAOEDINOEX FIBER<br />
Fig. 6.29<br />
A ruggedized fiberoptic cable connector.<br />
Courtesy Standard Telecommunications Laboratories<br />
Limited, Harlow, Essex, England;<br />
and ITT Cannon, Basingstoke, Hampshire,<br />
England.<br />
6.4 END-TEHMINa (RECEIVER) C0N51DEWT10N<br />
6-13
APPENDIX<br />
<strong>FIBEROPTIC</strong> <strong>SENSOR</strong>S GLOSSARY<br />
This Glossary on fiberoptic aensors is intended to<br />
provide definitions of the terms used in this Handbook<br />
and to provide supplementary information directly related<br />
to the topics discussed. Many topics that were<br />
introduced in the various chapters are developed in<br />
further detail in thia Glossary. l%is approach was used<br />
to avoid burdening the reader with details and explanations<br />
of terms aa topics were covered. For example,<br />
Maxwell’s equations, solid state electronics, electrooptic<br />
effects, electromagnetic theory, multiplexing<br />
and modulation methods, and various coefficient for<br />
transmission, reflection and attenuation are covered<br />
in this Gloasary.<br />
The definitions in this Glossary are consistent<br />
with international, national, Federal, military, and<br />
technical society atandards. Many were taken from the<br />
more comprehensive Fiberoptic and Lightwave Communications<br />
Standard Dictionary, Illustrated, 284 pages;<br />
and from the Communications Standard Dictionary,<br />
Illustrated. 1045 Dazes. .-. by . Martin H. Weik, Van<br />
Nostrand Reinhold Company, 135 W. 50th Street, New<br />
York, New York, 10020.<br />
A<br />
absorption. The transference of some or all of the<br />
energy contained in an electromagnetic wave to the<br />
substance or medium in which it ia propagating or<br />
upon which is is incident. Abaorbed energy from<br />
incident or transmitted lightwaves is converted into<br />
energy of other forms, usually heat, within the<br />
transmission medium, with the resultant attenuation<br />
of the intensity. See intrinsic absorption.<br />
acceptance angle. The maximum angle, measured from the<br />
longitudinal axis or centerline of an optical fiber<br />
to an incident ray, within which the incident ray<br />
will be accepted for transmission along the fiber,<br />
that is, total internal reflection of the incident<br />
ray occurs. If the acceptance angle for the fiber<br />
is exceeded, total internal reflection will not occur<br />
and the incident ray will be lost by leakage,<br />
scattering, diffuaion, or absorption in the cladding.<br />
The acceptance angle is dependent upon the<br />
refractive indicea of the two media that determine<br />
the critical angle. For a cladded fiber in air,<br />
the sine of the acceptance angle is given by the<br />
square root of the difference of the squares of the<br />
indices of refraction of the fiber core and ~he cla -<br />
ding. In mathematical notation, sine= (n -n<br />
7<br />
where 0 ia the acceptance angle, n, is tiie r~~l~c~<br />
tive index of the core, and n2 is the refractive<br />
index of the cladding. Synonymous with acceptance<br />
one-half angle.<br />
acceptance cone. A solid angle whose included apex<br />
angle is equal to twice the acceptance angle. Rays<br />
of light within the acceptance cone can be coupled<br />
into the end of an optical fiber and still maintain<br />
total internal reflection for all the rays in the<br />
cone. Typically, an acceptance cone is 40°.<br />
acceptance one-half angle.<br />
angle.<br />
Synonym for acceptance<br />
acceptor. In an intrinaic semiconducting material (such<br />
as galium arsenide), a dopant (such as germanium<br />
that has nearly the same electronic bonding structure<br />
as the intrinsic material, but with one less<br />
electron among its valence electrons than that required<br />
to complete the intrinsic bonding structural<br />
pattern. This pattern leaves a “space” or “hole”<br />
for one electron for each dopant atom in the structure.<br />
The dopant atoms are relatively few and are<br />
far apart and hence to not interfere with the electrical<br />
conductivity of the intrinsic material. An<br />
electron from a neighboring intrinsic material atom<br />
can fill the hole at the dopant site, leaving a hole<br />
from whence it came; thus, the hole can appear to<br />
move or wander about, although with less mobility<br />
than the electrons that are free and exceas to donor<br />
atoms. Also see donor; electron; hole.<br />
acoustooptic effect. The changes in diffraction gratings<br />
or phase patterns produced in a transm.lssion<br />
medium conducting a lightwave when the medium is<br />
subjected to a sound (acoustic) wave, due to the<br />
photoelaatic changes that occur. The acoustic waves<br />
might be created by a force developed by an impinging<br />
sound wave, the piezoelectric effect, or magnetostriction.<br />
The effect can be used to modulate a<br />
light beam in a material since many properties,<br />
such as lightconducting velocities, reflection and<br />
transmission coefficients at interfaces, acceptance<br />
angles, critical angles, and transmission modes,<br />
are dependent upon the diffractive changes that<br />
occur. The effect includea the phase transduction<br />
mechanism used in fiberoptic sensors, i.e., t h e<br />
change in phase that occurs due to the change in<br />
length and refractive index caused by the acoustic<br />
presaure. Also see electrooptic effect.<br />
acoustooptics. The study and application of the interrelation<br />
of acoustics and optics. Synonymous with<br />
optoacoustics.<br />
amplification by stimulated emission of radiation<br />
(laser). See light amplification by stimulated emission<br />
of radiation (laser).<br />
amplitude modulation (AM). The modulation of the amplitude<br />
of a wave serving as a carrier, by another wave<br />
serving as the modulating signal. The amplitude excursions<br />
of the carrier are made proportional to a<br />
parameter of the modulating signal that bears the<br />
information to be transmitted.<br />
A-1
angstrom. A unit of length equal to 10-10 meter, 10-1<br />
nanometer, and 10-4 micron.<br />
aperture. See numerical aperture (N. A. ).<br />
array.<br />
See sensor array.<br />
attenuation. The decrease in power of a signal, light<br />
beam, or lightwave, either absolutely or as a fraction<br />
of a reference value. The decrease usually<br />
occurs as a result of absorption, reflection, diffusion,<br />
scattering, deflection, or dispersion from<br />
an original level and usually not as a result of<br />
geometric spreading, i.e., the inverse sqwre of<br />
the distance. In an optical fiber, attenuation Is<br />
undesirable for transmission purposes but desirable<br />
for prevention of leakage or clandestine detection.<br />
Optical fibers have been classified as high-loss<br />
(over 100 dB/km), medium loss (20 to 100 db/km),<br />
and 10W1OSS (less than 20 dB/km).<br />
band.<br />
B<br />
See conduction band; energy band; valence band.<br />
bandwidth. 1. A range of frequencies, usually specifying<br />
the number of hertz of the band or the upper<br />
and lower limiting frequencies. 2. The range of<br />
. frequencies that a device is capable of generating,<br />
handling, passing, or allowing, usually the range<br />
of frequencies in which the response is not reduced<br />
greater than 3 dB from the maximum response.<br />
baseband. The band of frequencies associated with or<br />
comprising an original signal from a modulated<br />
source. In the process of modulation, the baseband<br />
is occupied by the aggregate of the transmitted signals<br />
used to modulate a carrier. In demodulation,<br />
it is the recovered aggregate of the transmitted<br />
signals. The termis commonly applied to cases where<br />
the ratio of the upper to the lower limit of the<br />
frequency band is large compared to unity.<br />
beam splitter. h optical device for dividing a light<br />
beam into two separated beams. One simple beam<br />
splitter consists of a plane parallel plate, with<br />
one surface coated with a dielectric or metallic<br />
coating that reflects a portion and transmits a portion<br />
of the incident beam; i.e., part of the light<br />
is deviated through an angle of 90°, and part iS<br />
unchanged in direction. A beam splitter may also<br />
be made by coating the hypotenuse face of a 45°-90”<br />
prism and cementing it to the hypotenuse face of<br />
another. The thickness of the metallic beam splitting<br />
interface will determine the proportions of the<br />
light reflected and transmitted. In metallic beam<br />
splitters, an appreciable amount of light is lost by<br />
absorption in the metal. It may also be necessary<br />
to match the reflected and transmitted beam for<br />
brightness and for color. In these cases, it is<br />
necessary to use a material at the interface that<br />
gives the same color of light by transmission and<br />
reflection. Nhere color matching at the surface or<br />
interface cannot be accomplished, a correcting color<br />
filter may be placed in one of the beams. In a<br />
fiber-to-fiber beam splitter, evanescent coupling<br />
can be used to transfer optical energy from one<br />
fiber to another.<br />
birefringence. The splitting of a light beam into two<br />
divergent components upon passage through a doublyrefracting<br />
transmission medium, with the two components<br />
propagating at different velocities in the<br />
medium. In an optical fiber, birefringence is related<br />
to the strain in the fiber which causes the<br />
fiber to be a single polarization transmission<br />
medium.<br />
Bragg cell. An acoustooptlc device that accepts fixed<br />
frequency monochromatic light and that has a baseband<br />
vibrating element capable of modulating the input<br />
lightwaves producing an output lightwave with a<br />
frequency equal to the frequency of the input lightwave<br />
plus the frequency of the baseband input signal.<br />
The Bragg cell has application as part of an interferometer<br />
in which heterodyne detection is used.<br />
Brewster angle. The angle, measured with respect to<br />
the normal, at which an electromagnetic wave incident<br />
upon an interface surface between two dielectric<br />
media of different refractive indices is totally<br />
transmitted into the second medium. The magnetic<br />
component of the incident wave must be parallel to<br />
the interface surfa~~l The Brewster angle is given<br />
by: tan B = (~2/E1)<br />
, where B is the Brewster angle,<br />
c1 is the electric permittivity of the incident<br />
medium, and e2 is the electric permittivity of the<br />
transmitted medium. The Brewster angle is a convenient<br />
angle to transmit all the energy in an optical<br />
fiber to an outside detector. There is no Brewster<br />
angle, for which there is total transmission and<br />
therefore zero reflection, when the electric field<br />
component is parallel to the interface, except when<br />
the permittivities are equal, in which case there<br />
is no interface. Mso, for entry into a more dense<br />
medium, such as from air into an optical fiber: tan<br />
B = (n2/nl), and from a more dense medium into a<br />
less dense medium, such as fiber to air: tan B =<br />
(nl/n2), where nl and n2 are the refractive indices<br />
of the air and fiber, respectively.<br />
brightfield sensor. In fiberoptic, a sensor in which<br />
the optical power modulated by the sensor is all or<br />
a large fraction of the total optical power fed to<br />
or available to the sensor. Synonymous with lightfield<br />
sensor. Contrast with darkfield sensor.<br />
budget. See optical power budget; power budget; risetime<br />
budget.<br />
bulk coupler. In fiberoptic, a coupler that has one<br />
input and many outputs.<br />
bundle jacket. The outer protective covering applied<br />
over a bundle of optical fibers.<br />
bus. 1. One or more conductors that serve as a common<br />
connection for a related group of devices. 2. One<br />
or more conductors used for transmitting optical or<br />
electrical power or signals.<br />
bend.<br />
See ordinary bend.<br />
bend loss.<br />
See microbend loss.<br />
A-2
c<br />
cable. 1. A jacketed bundle or jacketed fiber in a<br />
form that can be terminated. 2. A group of conductors<br />
that are bound together, usually with a protective<br />
sheath, a strength member, and insulation<br />
between individual conductors and for the entire<br />
group. See fiberoptic cable.<br />
cable jacket. The outer protective covering applied<br />
over the internal cable elements.<br />
carrier. 1. In communications, a wave, pulse train,<br />
or other signal suitable for modulation by an information-bearing<br />
signal to be transmitted over a communication<br />
system. 2. h unmodulated emission. A<br />
carrier is usually a sinusoidal wave, a recurring<br />
series of pulses, or a direct-current (DC) signal.<br />
See charge carrier.<br />
cavity.<br />
See resonant cavity.<br />
charge carrier. tin atomic or molecular particle that<br />
possesses an electric charge and is capable of moving<br />
under the influence of an electric or magnetic<br />
field. For example, an electron, a hole, or an ion.<br />
cladding. An optical transparent material, with a refractive<br />
index lower than that of the core, placed<br />
over or outside the core material of an optical<br />
waveguide that serves to reflect or refract lightwaves<br />
in order to confine them to the core. The<br />
cladding also serves to protect the core.<br />
cladding mode stripper. 1. A material applied to optical<br />
fiber cladding to allow light energy being<br />
transmitted in the cladding to leave the cladding of<br />
the fiber. 2. A piece of optical material or an<br />
optical component that can support only certain electromagnetic<br />
wave propagation modes. In particular,<br />
it does not support the propagation modes in the<br />
cladding of a cladded optical fiber, slab dielectric<br />
waveguide, or integrated optical circuit. The stripper<br />
effectively removes the cladding modes without<br />
disturbing the core-supported propagation modes.<br />
close-confinement junction. A synonym for single heterojunction.<br />
CMos.<br />
coating.<br />
See combined metal oxide semiconductor.<br />
See optical fiber coating.<br />
coherence length. The coherence time of a light beam<br />
multiplied by the velocity of the light, namely<br />
(1/cAv)c = l/Av. AI.SO see coherence time.<br />
coherence time. In beam of light propagating in a vacuum,<br />
the time obtained from the expression l/cAv,<br />
where c is the velocity of light in a vacuum, v is<br />
the reciprocal of the wavelength, and Avis the variation<br />
or spread of v over time for the beam. In<br />
material media, the c is replaced by c/n, where n is<br />
the refractive index. Also see coherence length.<br />
coherent bundle. A bundle of optical fibers in which<br />
the spatial coordinates of each fiber are the same<br />
or bear the same spatial relationship to each other<br />
at the two ends of the bundle. Synonymous with<br />
aligned bundle.<br />
coherent light. Light of which all parameters are predictable<br />
and correlated at any point in time or<br />
space, particularly over an area in a plane perpendicular<br />
to the direction of propagation or over time<br />
at a particular point in space. Contrast with<br />
incoherent light.<br />
collection angle.<br />
Synonym for acceptance angle.<br />
combined metal oxide semiconductor. A metal oxide semiconductor<br />
that consists of both positively-doped and<br />
negatively-doped material.<br />
common-mode. 1. Pertaining to any uncompensated combination<br />
of generator or receiver ground potential<br />
difference (voltage), generator common return offset<br />
voltage, and longitudinally-coupled peak random<br />
noise voltage measured between the receiver circuit<br />
ground and receiver cable with the generator ends<br />
of the cable short-circuited to ground. 2. The<br />
algebraic mean of the two voltages appearing at the<br />
receiver input terminals with respect to the receiver<br />
circuit ground. 3. Pertaining to the relative<br />
optical intensity fluctuations between two coherent<br />
electromagnetic (light) waves.<br />
common-mode rejection ratio (CMRR). The ratio of the<br />
common-mode interference voltage or optical intensity<br />
at the input of a circuit to the interference<br />
voltage or optical intensity at the output of the<br />
circuit.<br />
conduction band. In a semiconductor, the range of electron<br />
energy, higher than that of the valence band,<br />
possessed by electrons sufficient to make them free<br />
to move from atom to atom. When they leave the<br />
valence band, they are free to move under the influence<br />
of an applied electric field and thus they<br />
constitute an electric current.<br />
conductor. 1. In fiberoptic, a transparent medium<br />
that is capable of transmitting or conveying lightwaves<br />
a useful distance. 2. In electric circuits,<br />
a material that readily permits a flow of electrons<br />
through itself upon application of an electric field.<br />
Electrical conductors include copper, aluminum,<br />
lead, gold, silver, and platinum. The conductivity<br />
is specified by: J = aE, where J is the current<br />
density in amperes/square meter for S1 units, E is<br />
the applied electric field in volts/meter, and o is<br />
the conductivity in reciprocal ohms/meter. Also see<br />
dielectric. Contrast with insulator.<br />
connector. In fiberoptic, a device that permits the<br />
coupling of signals from one optical fiber or cable<br />
to another.<br />
connector insertion loss. The power loss sustained by<br />
a transmission medium, such as a wire, coaxial cable,<br />
optical fiber cable, or integrated optical circuit<br />
component, due to the Insertion of a connector between<br />
two elements, which would not occur if the<br />
media were continuous without the connector i.e.,<br />
if there were no reflected, absorbed, dispersed,<br />
or scattered power.<br />
controllable coupler.<br />
coupler.<br />
See electronically controllable<br />
A-3
core. The central primary light-conducting region of a<br />
material medium, such as an optical fiber, the refractive<br />
index of which must be higher than that of<br />
its cladding in order for the lightwaves to be<br />
totally reflected or refracted. Most of the optical<br />
power is in the core.<br />
coupler. In optical transmission aystems, a component<br />
used to interconnect two or more optical fibera.<br />
Also see connector; bulk coupler; electronic&llycontrollable<br />
coupler; reflective star-coupler; 3-dB<br />
coupler.<br />
coupling. The connection, attachment, or binding of<br />
optical elements, electric circuit elementa, electric<br />
and magnetic fields, propagation modes, or electromagnetic<br />
wave component, such as surface waves<br />
and evanescent waves, to internal waves in waveguides,<br />
dielectric slabs, or other interdependent<br />
associations and interactions of events and materials<br />
in a system. For example, two optical fibers or certain<br />
elements in an integrated optical circuit may<br />
be coupled together in some manner to preserve signal<br />
continuity. See evanescent field coupling.<br />
coupling coefficient. Synonym for coupling ratio.<br />
coupling efficiency. In fiberoptic transmission, the<br />
ratio of the optical power on one side of an interface<br />
to the optical power on the other side. For<br />
example, the ratio of the power developed by a light<br />
aource to the power accepted by a bundle of fibers,<br />
or the power received at the end of a bundle of<br />
fibers to the power that impinges on a photodetector.<br />
For light sources with emitting areas larger than<br />
fiber core diameters, the product of fiber numerical<br />
aperture (N.A.) and core diameter is a good indicator<br />
of maximum coupling efficiency. For other<br />
sources, such as small laser diodes with emitting<br />
areas small than the fiber core diameter, the N.A.<br />
alone is a relevant indicator of coupling efficiency,<br />
usually expresaed as a percentage.<br />
critical angle. The angle, with the normal, at which<br />
an electromagnetic wave incident upon an interface<br />
surface between two dielectric media, at which total<br />
reflection of the incident ray first occurs as the<br />
incident angle with the normal to the incident aurface<br />
is increased from zero, and beyond which total<br />
internal reflection continues to occur although with<br />
increased attenuation at a rate determined not only<br />
by the electromagnetic parameters of the transmission<br />
medium, but also by the frequency and the incidence<br />
angle. The wave is guided along the reflecting<br />
surface with no average transport of energy into<br />
the second medium, and the intensity of the reflected<br />
wave is exactly equal to the intensity of the<br />
incident wave. The wave in an optical fiber will<br />
be confined to the fiber for all incidence angles<br />
greater than the critical angle. The critical angle<br />
is given by sin ec = (~2/~1) 1/2 where 9C is the<br />
critical angle and Cz and c1 are the permittivities<br />
of the transmitted (outside) and incident medium<br />
(inside), respectively, and where El is always greater<br />
than =2; e.g. , the case for an optical fiber (conducting<br />
a wave), and air. In terms of refractive<br />
indices, the critical angle is the incidence angle<br />
from a denser medium, at an interface between the<br />
denser and less dense medium, at which all of the<br />
light is refracted along the interface, i.e., the<br />
angle of refraction is 90°. When the critical<br />
angle is exceeded, the light is totally reflected<br />
back into the denaer medium. The critical angle<br />
varies with the refractive indices of the two media<br />
with the relationship, sin Oc = n2/nl, where n2 is<br />
the index of refraction of the less dense medium, nl<br />
is the refractive index of the denser medium, and 9C<br />
is the critical angle, as above. In terms of total<br />
internal reflection in an optical fiber, the critical<br />
angle is the smallest angle made by a meridional<br />
ray in an optical fiber that can be totally reflected<br />
from the innermost interface and thus determines<br />
the maximum acceptance angle at which a meridional<br />
ray can be accepted for transmission along a fiber.<br />
Also see total internal reflection.<br />
critical radius. The largest radius of curvature of an<br />
optical fiber, containing an axially propagated<br />
electromagnetic wave, at which the field outside the<br />
fiber still detaches itself from the fiber and radiates<br />
into space because the phase-front velocity<br />
must increase to maintain a proper relationship with<br />
the guided wave inside the fiber. Thia velocity cannot<br />
exceed the velocity of light, aa the wavefront<br />
sweeps around the outside of the curved fiber. This<br />
causes attenuation due to a radiation loss. The<br />
field outside the fiber decays exponentially in a<br />
direction transverse to the direction of propagation.<br />
It is the radius of curvature of an optical<br />
fiber at which there is an appreciable propagation<br />
mode conversion loss, due to the abruptness of the<br />
transition from straight to curved. For a radius<br />
of curvature greater than the critical value, the<br />
fields behave essentially as in a straight guide.<br />
For radii smaller than the critical value, considerable<br />
mode conversion takea place.<br />
coupling loss. In a fiberoptic coupling, the optical<br />
power loss caused by the coupling itself, a loss<br />
that would not occur if the optical fiber were continuous<br />
without the coupling.<br />
coupling ratio. The ratio of power on the output side<br />
of a coupling to the power on the input side. The<br />
coupling ratio is always less than unity. Synonymous<br />
with coupling coefficient. Also see 3-dB coupler.<br />
A-4<br />
D<br />
dark current. ~’e current that flows in a photodetector<br />
when there is no radiant energy or luminous flux<br />
incident upon its aensitive surface, i.e., when there<br />
is total darkness. Dark current generally increaaea<br />
with increaaed temperature for most photodetectors.<br />
For example, in a photoemissive photodetector, the<br />
dark current is given by:<br />
Id = AT2eq’$lkT<br />
where A is the surface area constant, T is the absolute<br />
temperature, q is the electron charge, $ ia<br />
the work function of the photoemisaive surface material,<br />
and k is Boltzmann’s constant.<br />
darkfield sensor. In fiberoptic, a sensor in which<br />
the optical power tapped and modulated by the sensor<br />
is a small fraction of the total optical power fed<br />
to or available to the sensor. Contrast with brightfield<br />
sensor.<br />
data. Representation of facts, concepts, or instructions<br />
in a manner suitable for communication, interpretation,<br />
or processing by human, manual, semiautomatic,<br />
or fully-automatic means. The characters<br />
used as data may assume any form or pattern to which<br />
meaning may be assigned in order to represent infor-
mat ion. Data may be transferred or transported from<br />
place to place, auch as from city to city; from position<br />
to position, such as from coordinate poaition<br />
to coordinate position in the display space on the<br />
diaplay surface of a display device as display elements,<br />
display groups, or display images; or from<br />
location to location, such as in computer or buffer<br />
storage as characters or words. Data may be holes<br />
in tapes or cards; magnetized spots on discs, drums,<br />
tapes, cards, or chips; electrical current or voltage<br />
pulses in a wire; or modulated electromagnetic<br />
waves in free space or in optical fibers. Data may<br />
be presented on a CRT screen, a LED or gas panel, a<br />
fiberscope faceplate at the end of a coherent bundle<br />
of optical fibers, or other surface suitable for data<br />
display.<br />
data link. 1. A communication link suitable for transmission<br />
of data. The data link does not include the<br />
data source and the data sink. 2. TWO data stations<br />
and their connecting network, operating in<br />
such a manner that information can be exchanged bedata<br />
tween the stations. See fiberoptic link.<br />
— dB.<br />
dBV.<br />
dBm.<br />
See decibel.<br />
Decibel referred to one volt.<br />
Decibel referred to one milliwatt.<br />
decibel (dB). A gain or attenuation factor measured as<br />
10 times the logarithm to the base 10 of a power or<br />
acoustic energy ratio, or aa 20 timea the logarithm<br />
to the base 10 of the voltage or current ratio with<br />
reference to l-ohm impedance or pressure ratio. The<br />
ratio consists of a reference value as the ratio<br />
denominator and the value to be defined or measured<br />
as the numerator. If the logarithm is positive a<br />
gain is represented by decibels that are positive<br />
and if loss or attenuation is defined or measured,<br />
the decibels are negative. For example, if the ratio<br />
of optical power at the end of an optical to the<br />
power, at the beginning in 0.500, the 10SS iS expressed<br />
as 10 log 0.500 = -3.0103 dB., i.e., 3 dB<br />
down. Since the individual component gain or loss<br />
ratios introduced by serially connected cables, amplifiers,<br />
optical fibers, and other circuit or optical<br />
elements are multiplicative, the decibel gains<br />
and losses need only be added or subtracted according<br />
to sign. Thus, the mathematical relationships<br />
are:<br />
dB = 10 loglO(P1/P2)<br />
If R1=R2, then:<br />
= 10 loglo(E12/Rl)/E22/R2)<br />
= 10 loglo(112R1)/122R2)<br />
dB = 10 loglo(E12/E22) = 10 loglo(112/122)<br />
= 20 log10(E1/E2) = 20 loglo(I1/12)<br />
where P is the electrical or optical power, E is the<br />
electrical voltage, I is the electrical current, and<br />
R is the resistance or like impedance and the subscripts<br />
identify the two pointa of comparison of<br />
power, voltage, or current. The dB is one tenth the<br />
size of a bel, which is too large for convenient use.<br />
decollimation. In a lightwave guide, the spreading or<br />
divergence of light due to internal and end effects.<br />
Such effects include curvature, irregularities of<br />
surfaces, erratic variations in refractive indices,<br />
occlusions, and other blemishes that may cause dispersion,<br />
absorption, scattering, deflection, diffraction,<br />
reflection, and refraction.<br />
defect.<br />
See interstitial defect; vacancy defect.<br />
deflection. 1. A change in the direction of a traveling<br />
particle, usually without loss of particle kinetic<br />
energy, repreaenting a velocity change without<br />
a speed change. 2. A change in the direction of a<br />
wave, beam, or other entity, such as might be accomplished<br />
by an electric or magnetic field rather than<br />
by a prism (refraction), a mirror (reflection), or<br />
optical grating (diffraction).<br />
delay distortion.<br />
See waveguide delay distortion.<br />
demodulation. 1. To undo or reverse the effects of<br />
modulation; i.e., to remove the intelligence-bearing<br />
signal from a modulated carrier or to reconstitute<br />
the aignal that performed the modulation. 2. The<br />
process in which a modulated wave is processed to<br />
derive a wave having substantially the characteristics<br />
of the original modulating wave.<br />
density.<br />
See optical power density.<br />
depletion region. A region near a semiconductor junction<br />
in which there is a reduced concentration of<br />
charge carriers.<br />
detection. See heterodyne detection; homodyne detection;<br />
phase detection.<br />
detector. A device responsive to the presence of a<br />
stimulus. See photodetector.<br />
dielectric. Pertaining to material composed of atoms<br />
whose electrons are so tightly bound to the atomic<br />
nuclei that electric currents are negligible even<br />
under applied high electric fields. That is, scarcely<br />
any electrons of the material are in the conduction<br />
band; most remain in the valence band, even<br />
when high electric fields are applied, thua qualifying<br />
the material to be called an insulator. Conduction<br />
currents in dielectrics are nearly zero. Charges<br />
that might accumulate in one place tend to remain<br />
for relatively long periods of time. Most optical<br />
elements and optical fibers are dielectric. A transient<br />
polarization current occura only when an electric<br />
field is applied or removed, due to dipole<br />
rotation and alignment and polarization. Polarization<br />
and polarization currents are specified in<br />
Maxwell’s equationa by the electric permittivity,<br />
E, of dielectric materials. Also see conductor.<br />
See slab dielectric op-<br />
dielectric optical waveguide.<br />
tical waveguide.<br />
dielectric waveguide.<br />
See alab dielectric waveguide.<br />
A-5
diffraction. 1. The procesa by which the propagation<br />
of radiant waves or lightwaves are modified as the<br />
waves interact with objects or obstacles. Some of<br />
the rays are deviated from their path by diffraction<br />
at the objects, whereaa other rays remain undeviated<br />
by diffraction at the objects. As the objects become<br />
small in comparison with the wavelength, the<br />
concepts of reflection and refraction become useless,<br />
and diffraction plays the dominant role in determining<br />
the redistribution of the rays following incidence<br />
upon the objects. Diffraction results from<br />
the deviation of light from the paths and foci prescribed<br />
by the rectilinear propagation laws of geometrical<br />
optics. Thus, even with a very small, distant<br />
source, some light, in the form of bright and<br />
dark bands, is found within a geometrical shadow<br />
because of the diffraction of the light at the edge<br />
of the object forming the shadow. Diffraction gratings,<br />
with spacings of the order of the wavelength<br />
of the incident light also cause diffraction that<br />
results in the formation of light and dark areas<br />
called “diffraction patterns.” Such gratings can<br />
be ruled grids, spaced spots, or crYstal lattice<br />
structures. 2. The bending of radio, sound, or<br />
lightwaves around an object, barrier, or aperture<br />
edges.<br />
diode. See light-emitting diode (LED).<br />
dispersion. 1. The process by which rays of light of<br />
different wavelength are deviated angularly by different<br />
amounts; e.g. , as with prisms and diffraction<br />
gratings. 2. Phenomena that cause the refractive<br />
index and other optical properties of a transmission<br />
medium to vary with wavelength, also refers to the<br />
frequency dependence of any of several parameters,<br />
for example, in the process by which an electromagnetic<br />
signal is distorted because the various frequency<br />
components of that signal have different propagation<br />
characteristics and paths. Thus, the components<br />
of a complex radiation are dispersed or<br />
separated on the basis of some characteristic. A<br />
prism disperses the components of white light by<br />
deviating each wavelength a different amount. For<br />
example, 2.5 nsec/km might be a maximum allowable<br />
dispersion for an 18.7 Mbit/see pulse repetition<br />
rate with 10 km repeater spacing. 3. The allocation<br />
of circuits between two points over more than<br />
one geographic or physical route. See intermodal<br />
dispersion; intramodal dispersion; material dispersion;<br />
modal dispersion; waveguide dispersion.<br />
distortion.<br />
See waveguide delay distortion.<br />
diversity. See polarization diversity.<br />
donor. In an intrinsic semiconducting material, a dopant<br />
that has nearly the same electronic bonding<br />
structure as the intrinsic material, but with one<br />
more electron among its valence electrons than that<br />
required to complete the intrinsic bonding pattern,<br />
thus leaving one “extra” or “excess” electron for<br />
each impurity (dopant) atom in the structure. The<br />
dopant (i.e., the donor) atoms are relatively few<br />
and far apart and hence to not interfere with the<br />
electrical conductivity of the intrinsic material.<br />
Tin or tellurium can serve as a dopant for galium<br />
arsenide. The extra electron moves or wanders from<br />
atom to atom more freely than the bound electrons<br />
that ar required to complete the bonding structure,<br />
although interchanges actually occur with the bound<br />
electrons. The extra electrons move about more<br />
freely than the holes created by acceptors. Hence,<br />
the electrons are more mobile than the holes. Under<br />
A-6<br />
the influence of electric fields, the electrons and<br />
holes move in the direction of the field according<br />
to their sign, thus constituting an electric current.<br />
Also see acceptor; electron; hole.<br />
E<br />
electromagnetic interference. Interference caused or<br />
generated in a circuit by electromagnetic radiation<br />
energy coupling. The radiation may be lightwaves,<br />
radio waves, gamma rays, high-energy neutrons, x-<br />
rays, or microwaves. Sources include artifical<br />
transmissions and emissions as well as natural<br />
sources, such as cosmic and solar sources. The<br />
phenomenon of interference is considered to occur<br />
when electromagnetic energy causes an unacceptable<br />
or undesirable response, malfunction, degradation,<br />
or interruption of the intended operation or performance<br />
of electronic equipment.<br />
electromagnetic pulse (EMP). A broadband, high-intensity,<br />
short-duration burst of electromagnetic energy,<br />
such as might occur from a nuclear detonation.<br />
In the case of a nuclear detonation, the electromagnetic<br />
pulse (signal) consists of a continuous spectrum<br />
with most of its energy distributed throughout<br />
the lower frequencies between 3 Hz and 30 kHz.<br />
electromagnetic wave (EMW). The effect obtained when a<br />
time-varying electric field and a time-varying magnetic<br />
field interact, causing electrical and msgnetic<br />
energy to be propagated in a direction that is<br />
dependent upon the spatial relationship of the two<br />
interacting fields that are interchanging their energies.<br />
The most common EMU consists of time-varying<br />
electric and magnetic fields that are directed at<br />
right angles to each other, thus defining a plane in<br />
which they both lie, i.e., polarization plane. The<br />
direction of energy propagation is perpendicular to<br />
this plane, and the wave is called plane polarized.<br />
A plane-polarized wave may be linearly, circularly,<br />
or elliptically polarized depending on the phase<br />
relationship between the varying electric and msgnetic<br />
fields. When launched initially, the interacting<br />
and interrelated time-varying electric and magnetic<br />
fields are produced by an electric current,<br />
consisting of moving electric charges that oscillate<br />
in time and space, such as might oscillate In a wire,<br />
called an antenna. If an electric field is made to<br />
vary in time in a conductive medium in order to produce<br />
an oscillating current, an electromagnetic wave<br />
will be launched that can propagate energy through<br />
material media and a vacuum. If the time and spatial<br />
distributions of currents are given, the electromagnetic<br />
field intensities, power flow rates, and energy<br />
densities can be determined everywhere in space, provided<br />
also that the parameters of the material in<br />
the space are known. Lightwaves are electromagnetic<br />
waves that can travel in optical fibers where they<br />
can be trapped and guided, and can be made to energize<br />
photodetectors.<br />
electron. A basic negatively charged particle with a<br />
char e of 1.6021 x 10-19 C and a mass of 9.1091 x<br />
10-3 f kg. It is outside the nucleus of the chemical<br />
elements, exists with different discrete energy<br />
levels in a given chemical element, differentiates<br />
the elements by its population outside the nucleus,<br />
and is the moving matter that contributes the most<br />
to the formation of electric currents and voltages.<br />
Also see acceptor; donor; hole.
electron-hole recombination. The combining of an electron<br />
and a hole resulting in a decrease in electron<br />
energy and the production of a photon.<br />
electronically-controllable coupler. An optical element<br />
that enables other optical elements to be coupled<br />
to, or uncoupled from, each other, in accordance<br />
with an applied electrical signal. For example, two<br />
parallel slab dielectric waveguides with an optical<br />
material between them whose refractive index can be<br />
altered by application of an electronic signal, thus<br />
turning the coupling of the waveguides on or off according<br />
to the signal.<br />
electrooptic coefficient. A measure of the extent to<br />
which the refractive index changes with applied high<br />
electric field, auch as several parts per 10 thousand<br />
for applied fields of the order of 20 V/cm.<br />
Since the phase shift of a lightwave is a function<br />
of the refractive index of the transmission medium<br />
in which it is propagating, the change in index can<br />
be used to phase-modulate the lightwave by shifting<br />
its phase at a particular point along the guide, by<br />
changing propagation time to the point.<br />
electrooptic device. 1. An electronic device that uses<br />
electromagnetic radiation in the visible, infrared,<br />
or ultraviolet regions of the frequency spectrum;<br />
emits or modifies noncoherent or coherent electromagnetic<br />
radiation in these same regions; or uaes<br />
such electromagnetic radiation for its internal operation.<br />
The wavelengths handled by theae devices<br />
range from approximately 0.3 to 30 microns. 2. Electronic<br />
devices associated with light, aerving aa<br />
sources, conductors, or detectors. Synonymous with<br />
optoelectronic device.<br />
electrooptic effect. The change in the refractive index<br />
of a material when subjected to an electric field.<br />
It can be used to modulate a light beam in a mater–<br />
ial since many light propagation properties are dependent<br />
upon the refractive indices of the transmission<br />
medium in which the light travels.<br />
electrostrictive effects. The change in physical dimensions<br />
that occurs to certain materials when they are<br />
placed in an electric field.<br />
EMI.<br />
EMP.<br />
emission.<br />
See electromagnetic interference.<br />
See electromagnetic pulse.<br />
See spontaneous emission.<br />
emission of radiation. See light amplification by stimulated<br />
emiasion of radiation (laser).<br />
energy band. A specified range of energy levels that a<br />
constituent particle or component of a substance may<br />
have. The particles are uaually electrons, protons,<br />
ions, neutrons, atoms, or molecules. Some energy<br />
bands are allowable and some are unallowable for<br />
specific particles. For example, electrons of a<br />
given element at a specific temperature occupy only<br />
certain energy bands. Examples of energy bands are<br />
the higher and lower level ranges of the conduction<br />
and valence bands.<br />
energy gap. The difference in energy level between the<br />
lower limit of the conduction band and the upper<br />
limit of the valence band.<br />
energy level. The discrete precise amount of kinetic<br />
and potential energy possessed by a body, such as an<br />
orbiting electron. A quantum of energy is absorbed<br />
or radiated depending on whether an electron moves<br />
from a lower to a higher energy level or vice versa.<br />
evanescent-field coupling. Coupling between two waveguides,<br />
auch as an optical fiber or an integrated<br />
optical-circuit (IOC), in which the waveguides are<br />
held parallel to each other in the coupling region,<br />
with the evanescent waves on the outside of one of<br />
the waveguides entering the coupled waveguide, bringing<br />
some of the light energy with it into the coupled<br />
waveguide. In optical fibers and planar dielectric<br />
waveguides, close-to-core proximity or fusion<br />
is required. The evanescent field of the core modes<br />
can be made available by etching away the fiber<br />
cladding or locally modifying the refractive index.<br />
evanescent wave. In a waveguide conducting a transverse<br />
electromagnetic wave, the wave on the outside of the<br />
guide. It will radiate away at sharp bends in the<br />
guide if the radiua of the bend is less than the<br />
critical radius. It uaually has a frequency smaller<br />
than the cutoff frequency above which true propagation<br />
occurs and below which the waves decay exponentially<br />
with distance from the guide. Evanescent<br />
wavefronts of constant phase may be perpendicular<br />
or at an angle less than 90” to the surface of the<br />
guide.<br />
extrinsic fiber loss. Optical power loss in an optical<br />
fiber aplice, connector, or coupling caused by end<br />
separation, axial displacement, axial misalignment,<br />
reflection, or other external condition involved in<br />
implementation or use and subject to the control of<br />
the uaer.<br />
F<br />
Fabry-Perot interferometer. A high-resolution multiple-beam<br />
interferometer consisting of two optically<br />
flat and parallel glasa or quartz plates held a short<br />
fixed diatance apart, the adjacent aurfaces of the<br />
platea or interferometer flata being made almoat<br />
totally reflecting by a thin silver film or multilayer<br />
dielectric coating. If one plate is moved with<br />
respect to the other, interference patterns are produced.<br />
If the ends of an optical fiber are made reflective,<br />
moving one end with reapect to the other<br />
will also result in an output signal when monochromatic<br />
light is inserted into the fiber.<br />
Faraday effect.<br />
FDM.<br />
Synonym for magnetooptic effect.<br />
See frequency-division multiplexing.<br />
fiber. See graded-index fiber; low-loss fiber; multimode<br />
fiber; optical fiber; SELFOCc fiber; self-focusing<br />
optical fiber; single-mode fiber; step-index<br />
fiber; optical-fiber coating.<br />
fiber length-bandwidth product. The product of the<br />
length of an optical fiber and the spectral width of<br />
lightwavea propagating within it, usually expressed<br />
in micron-kilometers.<br />
fiber loss. See extrinsic fiber loss; intrinsic fiber<br />
loss; optical fiber loss.<br />
A-7
fiberoptic. Pertaining to optical fibers and the systems<br />
in which they are used, such as sensor, telemetry,<br />
and telecommunication systems.<br />
fiberoptic cable. Optical fibers incorporated into an<br />
assembly of materials that provides tensile strength,<br />
external protection, and handling properties comparable<br />
to those of coaxial cables. Fiberoptic cables<br />
(light guides) are a direct replacement for conventional<br />
coaxial cables and wire pairs. The glassbased<br />
transmission facilities occupy far less physical<br />
volume for an equivalent transmission capacity,<br />
which is a major advantage in crowded underground<br />
ducts. Manufacturing, installation, and maintenance<br />
costs are less. These advantages, with the reduced<br />
use of critical metals, such as copper, is a strong<br />
impetus for the use of fiberoptic cables.<br />
fiberoptic data link. A data link, consisting of a modulated<br />
light source, a fiberoptic cable, and a<br />
photodetector, that can handle signals in the form<br />
of a modulated lightwave. Synonymous with optical<br />
data link.<br />
fiberoptic ribbon.<br />
Synonym for optical fiber ribbon.<br />
fiberoptic (FO). 1. As first defined by Kapany in<br />
1956, the art of the active and passive guidance of<br />
light (rays and waveguide modes) in the ultraviolet,<br />
visible, and infrared regions of the spectrum along<br />
transparent fibers through predetermined paths. 2.<br />
The technology of guidance of optical power, including<br />
rays and waveguide modes of electromagnetic<br />
waves along conductors of electromagnetic waves in<br />
the visible and near-visible region of the frequency<br />
spectrum, specifically when the optical energy is<br />
guided to another location through thin transparent<br />
strands. Techniques include conveying light or<br />
images through a particular configuration of glass<br />
or plastic fibers. Incoherent optical fibers will<br />
transmit light, as a pipe will transmit water, but<br />
not an image. Coherent optical fibers can transmit<br />
an image through small (2-12 microna diameter), clad,<br />
optical fibers that are in a fixed spatial relative<br />
position at both ends. Specialty fiberoptic combine<br />
coherent and incoherent aspects.<br />
fiberoptic sensor. A sensor in which a parameter (property,<br />
characteristic) of an optical waveguide (optical<br />
fiber), or of a lightwave propagating in an<br />
optical fiber, is varied in accordance with an input<br />
baseband signal thus modulating the lightwave in the<br />
waveguide. Synonymous with optical fiber sensor;<br />
optical sensor. Also see sensor.<br />
fiberoptic sheath. An outer protective covering placed<br />
over an optical fiber, bundle, or cable.<br />
fiberoptic splice. A nonseparable junction joining one<br />
optical conductor to another.<br />
fiber ribbon.<br />
See optical fiber ribbon.<br />
fiberscope. A receiving device consisting of an entry<br />
point, at which a bundle of optical fibers can enter,<br />
and a faceplate surface on which the entering fibers<br />
can uniformly terminate, in order to display the optical<br />
image received through the fibers. The bundle<br />
of fibers transmit a full color image that remains<br />
undisturbed when the bundle is bent. By mounting<br />
an objective lens on one end of the bundle and an<br />
eyepiece at the other, the assembly becomes a flexible<br />
fiberscope that can be used to view objects that<br />
are otherwise Inaccessible for direct viewing. The<br />
transmitter is a similar device, except that an image<br />
is focused on it for transmission. The device is<br />
used to transmit images. Also see coherent bundle.<br />
fiber sensor. See fiberoptic sensor.<br />
field coupling.<br />
See evanescent field coupling.<br />
focusing optical fiber. See self-focusing optical<br />
fiber.<br />
frequency-division multiplexing (FDM). Multiplexing in<br />
which the available transmission frequency range is<br />
divided into narrower bands, each used as a separate<br />
channel. When an optical fiber transmits more than<br />
one frequency at the same time, each frequency can<br />
be modulated with a different information-bearing<br />
signal.<br />
frequency modulation. The modulation of the frequency<br />
of an electromagnetic, elastic, sound, or other wave<br />
serving as a carrier, with another wave serving as<br />
the modulating signal, such that the frequency excursions<br />
of the carrier are proportional to a parameter<br />
of the modulating signal bearing the information<br />
to be transmitted. It is a form of angle modulation<br />
in which the instantaneous frequency of a<br />
aine wave carrier is caused to depart from the carrier<br />
frequency by an amount that is proportional to<br />
the instantaneous value of the modulating signal.<br />
Combinations of phase and frequency modulation are<br />
also considered as frequency modulation.<br />
Fresnel equations. See reflection coefficient, transmission<br />
coefficient.<br />
E!-Fl”<br />
See energy gap.<br />
G<br />
geometric spreading. In a wave propagating in a transmission<br />
medium in which there are no sources, the<br />
decrease in power density as a function of distance<br />
in the direction of propagation. As a curved wavefront,<br />
such as for divergent electromagnetic waves,<br />
moves in the direction of propagation, the available<br />
power at one point must be spread over a larger area<br />
at the next point in space; e.g., a point source of<br />
light has its light energy spread over larger and<br />
larger spherical surfaces as the distance from the<br />
source increases.<br />
graded-index fiber. An optical fiber witb a variable<br />
refractive index that is a function of the radial<br />
distance from the fiber axis, the refractive index<br />
getting progressively lower away from the axis. This<br />
characteristic causes the light rays to be continually<br />
refocused by refraction in~o the core. As a<br />
result, there is a designed continuous change in<br />
refractive index between the core and cladding along<br />
a fiber diameter. Synonymous with gradient-index<br />
fiber.<br />
gradient-index fiber. A synonym for graded-index fiber.<br />
A-8
group velocity. The velocity of propagation of the envelope<br />
produced when an electromagnetic wave is modulated<br />
by, i.e., mixed with, another wave of a different<br />
frequency. The group velocity is the velocity<br />
of information propagation and, loosely, of energy<br />
propagation. It is the velocity of transmission<br />
of energy associated with a progressing wave consisting<br />
of a group of sinusoidal components; i.e., the<br />
velocity of a certain feature of the wave envelope,<br />
e.g., the crest. The group velocity differs from<br />
the phase velocity. Only the latter varies with<br />
frequency. In general, the group velocity, representated<br />
as:<br />
is less than the phase velocity, represented as;<br />
‘P “<br />
IJJ/i3<br />
where B is the angular velocity, ( u= 2n’f) and u is<br />
the propagation constant.<br />
guide.<br />
See waveguide.<br />
H<br />
heterodyne detection. In fiberoptic, detection based<br />
on the use or mixing of two or more frequencies.<br />
For example, if a lightwave is fed to a Bragg cell,<br />
it produces an output lightwave frequency that is<br />
the sum of the input lightwave frequency and the<br />
baseband frequency; an interferometer can be used to<br />
recover the baseband frequency.<br />
heterodyning. The mixing of an electromagnetic wave of<br />
one frequency with a wave of another frequency to<br />
produce one or more additional frequencies. Usually<br />
the sum and difference frequencies will be produced<br />
when waves of two different frequencies are combined<br />
in a nonlinear device, such as a nonlinear amplifier.<br />
heterojunction. In a laser diode, a boundary surface<br />
at which a sudden transition occurs in material composition<br />
across the boundary. For example, in a<br />
semiconductor, a change in the refractive index as<br />
well as a change from a positively-doped (p) region<br />
to a negatively-doped (n) region; or a positivelydoped<br />
region with a rapid change in doping level,<br />
i.e., a high concentration gradient of dopant versus<br />
distance. In most heterojunctions, change in geo -<br />
metric cross-section occurs across which a voltage<br />
or voltage barrier exists. Heterojunctions provide a<br />
controlled level and direction of radiation confinement.<br />
There usually is a step in the refractive<br />
index level at each heterojunction. Contrast with<br />
homojunction. See single heterojunction.<br />
hole. In physical electronics and solid-state devices,<br />
a semiconducting material containing a dopant that<br />
has one less electron for each atom than that required<br />
to complete the intrinsic bonding structure,<br />
a site at which an electron is missing to complete<br />
the bonding structure. Initially, the hole is created<br />
by the impurity atoms, but if an electron from a<br />
neighboring atom moves in to “fill” the hole, the<br />
neighboring atom will have a hole; thus, the hole<br />
can be considered to have migrated. Also see acceptor;<br />
donor; electron.<br />
homodyne detection. In fiberoptic, detection based on<br />
the use of only one frequency. For example, a detector<br />
that makes use of a varying-length fiber to achieve<br />
modulation of the phase of the lightwave at<br />
the output end of the fiber; the input baseband signal<br />
modulates the length of the fiber and thus there<br />
is no change in frequency of the lightwave.<br />
homogeneous medium. In optical systems, a transmission<br />
medium whose light-transmission parameters, such as<br />
the parameters of the constitutive relations, are<br />
spatially constant and not a function of space coordinates,<br />
although they may vary as a function of<br />
time, temperature, pressure, humidity, or other parameter<br />
uniformly throughout the medium.<br />
homojunction. In a laser diode, a single junction; i.e.,<br />
a single region of shift in doping from positive to<br />
negative majority carrier regions, or vice versa,<br />
and a change in refractive index, all at one boundary.<br />
Hence one energy-level shift, one barrier, and<br />
one refractive-index shift constitute a aingle homojunction.<br />
Constrast with heterojunction.<br />
I<br />
incident ray. A ray of light that falls upon, or<br />
strikes, the surface of any object. The ray is said<br />
to be incident at the surface.<br />
incoherent light. Light of which not all parameters<br />
are predictable and correlated at any point in time<br />
or space, such as scattered or diffused light.<br />
Contrast with coherent light.<br />
index.<br />
See refractive index.<br />
index profile. See radial refractive index profile.<br />
See refractive-index-pro-<br />
index-profile mismatch loss.<br />
file mismatch loss.<br />
index profile parameter.<br />
parameter.<br />
See refractive index profile<br />
index-matching material. Alight-conducting material<br />
used in intimate contact with optical components<br />
such as optical fibers and lenses, to reduce optical<br />
power losses by using materials with refractive indices<br />
at interfaces that will reduce reflection,<br />
increase transmission, avoid scattering, and reduce<br />
dispersion.<br />
insertion loss. 1. In a communication system, the decrease<br />
in signal level that results from the insertion<br />
of a series component in a transmission circuit.<br />
It is expressed as a percent, in decibels, or as a<br />
per unit coefficient or fraction. The loss may be<br />
positive or negative, that is, greater or less than<br />
unity when expressed as a ratio (per unit fraction<br />
or coefficient). If the insertion loss is negative<br />
it is considered as a gain. When it is expressed<br />
as a fraction, ratio, or per unit, it is the decrease<br />
in signal level caused by the insertion divided by<br />
the signal level before insertion. 2. In an optical<br />
fiber, the optical power loss due to all causes,<br />
usually expressed as decibels/kilometer. Causes of<br />
loss may be absorption, scattering, diffusion, leaky<br />
modes, dispersion, microbending, or other causes or<br />
A-9
methods of coupling power outside the fiber. For<br />
example, in an optical component such as a 3-dB<br />
coupler, the insertion loss is considered as that<br />
in excess of the 3-dB associated with splitting the<br />
light between two fibers. 3. In lightwave transmission<br />
systems, the power lost at the entrance to<br />
a wavegufde due to any and all causes, such as<br />
Fresnel reflection, packing fraction, limited numerical<br />
aperture, axial misalignment, lateral displacement,<br />
initial scattering, or diffusion.<br />
insulator. A substance with a molecular structure in<br />
which all electrons remain in the valence band,<br />
rather than in the conduction band, even under the<br />
influence of high electric field gradients, and<br />
therefore a material that is used to prevent the<br />
flow of electric current when electric fields exist.<br />
tiso see dielectric. Contrast with conductor.<br />
integrated optical circuit (IOC). A circuit, or group<br />
of interconnected circuits, consisting of miniature<br />
solid state optical components. Examples of such<br />
components include light-emitting diodes, optical<br />
filters, photodetectors (active and passive), and<br />
thin-film optical waveguides on semiconductor or dielectric<br />
substrates. Components onan IOC chip might<br />
include semiconductor injection lasers, modulators,<br />
filters, lightguides, switches, couplers, logic<br />
gates, pulse shapers, differential amplifiers, and<br />
optical memories. Synonymous with optical integrated<br />
circuit.<br />
integrated optics. The design, development, and operation<br />
of circuits that apply the technology of integrated<br />
electronic circuits produced by planar masking,<br />
etching, evaporation, and crystal film growth<br />
techniques to microoptical circuits on a single<br />
planar dielectric substrate. Thus, a combination<br />
of electronic circuitry and optical waveguides are<br />
produced for performing various communication,<br />
switching, and logic functions, including amplification,<br />
gating, modulating, light generation, photodetecting,<br />
filtering, multiplexing, signal processing,<br />
coupling, and storing.<br />
intensity.<br />
See luminous intensity.<br />
intensity sensor. In fiberoptic, a fiberoptic sensor<br />
in which the optical intensity of a light ray (beam)<br />
is varied in accordance with a baseband signal by<br />
varying the light propagation properties of an optical<br />
fiber. For example, a microbend sensor.<br />
interference.<br />
See electromagnetic interference.<br />
interferometer. An instrument in which the interference<br />
effects of lightwaves are used for purposes of<br />
measurement, such as the measurement of the accuracy<br />
of optical surfaces by means of Newton’s rings, the<br />
measurement of optical paths, linear and angular<br />
displacements, phase changes due to pressure, rotation,<br />
and temperature effects on the sensing arm as<br />
compared to the reference arm. See Fabry-Perot<br />
interferometer; Mach-Zehnder interferometer; Michelson<br />
interferometer; Sagnac interferometer; _n-<br />
Green interferometer.<br />
interferometric sensor. In fiberoptic, a fiberoptic<br />
sensor that employs the principles of interferornetry<br />
to performa sensing function. For example, aFabry-<br />
Perot interferometer used as a fiberoptic sensor.<br />
Also see interferometer.<br />
interferometry. The scientific discipline devoted to<br />
the study and useful application of interference<br />
among electromagnetic waves.<br />
intermodal disperson. Dispersion (pulse broadening)<br />
that results from propagation time differences among<br />
the various modes in an electromagnetic pulse. Intermodal<br />
dispersion can be reduced by appropriate refractive<br />
index profile shaping.<br />
internal reflection. In an optical element in which an<br />
electromagnetic wave is propagating, a reflection at<br />
an outside surface from the inside such that a wave<br />
that is incident upon the surface is reflected wholly<br />
or partially back into the element itself. Optical<br />
fibers depend on internal reflection for the successful<br />
transmission of lightwaves in order that the<br />
waves do not leave the fiber; namely, the wave energy<br />
is confinded to or bound to the fiber. Also see<br />
total internal reflection.<br />
internal reflection sensor. See near total internal reflection<br />
sensor.<br />
interstitial defect. In the somewhat ordered array of<br />
atoms and molecules in optical fiber material, a<br />
site at which an extra atom or molecule is inserted<br />
in the space between the normal array. The defect<br />
can serve as a scattering center, causing diffusion,<br />
heating, absorption, and resultant attenuation. Also<br />
see vacancy defect.<br />
intrinsic absorption. In lightwave transmission media,<br />
the absorption of light energy from a traveling or<br />
standing wave by the medium itself, causing attenuation<br />
as a function of distance, material properties,<br />
mode, frequency, and other factors. Intrinsic absorption<br />
is primarily due to charge transfer bands<br />
in the ultraviolet region and vibration or multiphonon<br />
bands in the near infrared, particularly if<br />
they extend into the region of wavelengths used in<br />
optical fiber, namely, 0.7 to 1.2 microns.<br />
intramodal dispersion. The dispersion (pulse broadening)<br />
that occurs within one of the modea in an electromagnetic<br />
pulse. Intramodal dispersion in an optical<br />
fiber is a function of the spectral bandwidth<br />
of the light source and the material dispersion<br />
caused by the fiber. It is usually the only type of<br />
dispersion preaent in a monomode fiber.<br />
intrinsic fiber loss. Optical power loss in an optical<br />
fiber or optical fiber splice, connector, or coupling,<br />
caused in the manufacturing process, such as<br />
refractive index profile mismatch, diameter differences,<br />
scattering, absorption, and other causes not<br />
subject to the control of the user.<br />
intrinsic region. In a semiconductor junction, a region<br />
that lies between a positively-doped region and a<br />
negatively-doped region and that does not contain<br />
any dopant. Synonymous with i-region.<br />
inversion.<br />
See population inversion.<br />
Ioc. See integrated optical circuit.<br />
i-region.<br />
Synonym for intrinsic region.<br />
A-10
isotropic material. A substance that exhibits the same<br />
property when tested along an axis in any direction.<br />
For example, a dielectric material with the same<br />
permittivity to electric fields, a glass with the<br />
same refractive index for a lightwave, or the same<br />
conductivity to electric currents, in all directions.<br />
jacket.<br />
See heterojunction; homojunction; p-n junc-<br />
junction.<br />
tion.<br />
See bundle jacket; cable jacket.<br />
J<br />
K<br />
Kerr cell. A substance, usually a liquid, whose refractive<br />
index change is proportional to the square of<br />
an applied electric field. If the substance is configured<br />
to be part of an optical path, the cell can<br />
provide a means of modulating the light in the optical<br />
path.<br />
L<br />
lasing. A phenomenon occurring when resonant frequency<br />
controlled energy is coupled to a specially prepared<br />
material, such as a uniformly-doped semiconductor<br />
crystal that has free-moving or highly mobile loosely-coupled<br />
electrons. AS a result of resonance and<br />
the imparting of energy by collision or close approach,<br />
electrons are raised to highly excited energy<br />
states, which, when they move to lower states, cause<br />
quanta of high-energy electromagnetic radiation to<br />
be released as coherent lightwaves. This action<br />
takes place in a laser.<br />
LED.<br />
length.<br />
See light emitting diode.<br />
See coherence length.<br />
length-bandwidth product.<br />
product.<br />
See fiber length-bandwidth<br />
light. See coherent light; incoherent light; polarized<br />
light.<br />
light amplification by stimulated emission of radiation<br />
(lasers). A coherent-light generator in which molecules<br />
of certain substances absorb incident electromagnetic<br />
energy at specific frequencies, store the<br />
energy for short periods in higher energy-band levels<br />
and then release the energy, upon their return to<br />
the lower energy levels, in the form of light at particular<br />
frequencies in extremely narrow frequency<br />
bands. The release of energy can be controlled in<br />
time and direction so as to generate an intense<br />
highly directional narrow beam of electromagnetic<br />
energy that is coherent, i.e., the electromagnetic<br />
fields at every point in the beam are uniquely and<br />
specifically definable. Diode lasers and heliumneon<br />
lasers make use of a resonant cavity that is<br />
pumped to high energy levels to cause Population<br />
inversion and lasing action.<br />
rate, and the same operational current densities,<br />
but without lasing action. The high current densities<br />
of thousands of amperes per square centimeter<br />
often cause catastrophic and graceful degradation.<br />
Compared to the laser diode, the LED possesses<br />
greater simplicity, tolerance, and ruggedness, and<br />
about 10 times the spectral width. Typical peak<br />
spectral power output for a gallium arsenide LED<br />
occurs at 0.910 pm (microns), with a spectrum about<br />
0.005 pm wide. An aluminum arsenide LED operates at<br />
0.820 pm at a 10-MHz-wide spectrum. Both operate at<br />
roughly l-mW spectral power output and a 50-mA<br />
driving current.<br />
lightfield sensor.<br />
Synonymous with brightfield sensor.<br />
light pipe. 1. An optical element that conducts light<br />
from one place to another, such as an optical fiber<br />
or slab-dielectric waveguide. 2. A hollow tube with<br />
a reflecting inner wall that guides lightwaves in<br />
its hollow center. 3. An optical fiber.<br />
light ray. A line perpendicular to the wave-front of a<br />
lightwave indicating its direction of propagation<br />
and representing the lightwave itself.<br />
light source. A device that produces or emits lightwaves,<br />
such as a light-emitting diode, a laser, or a<br />
lamp.<br />
linear medium. An electromagnetic wave transmission<br />
medium with constitutive parameters, such as electric<br />
permittivity, magnetic permeability, and electric<br />
conductivity (and hence refractive index), that remain<br />
constant under the influence of applied electric<br />
and magnetic fields. For example, in the relations<br />
B=uH, D=cE, andJ=uE, thep, e, a nd u are constant<br />
at a given point even though the fields are<br />
changing.<br />
link. See data link; fiberoptic data link.<br />
lock 100P.<br />
w“<br />
See phase-lock loop.<br />
See phase-lock loop.<br />
loss. See coupling loss; extrinsic fiber loss; insertion<br />
loss; intrinsic fiber 10SS; microbending 10SS;<br />
optical fiber loss; refractive-index-profile mismatch<br />
loss.<br />
low-loss fiber. AII optical fiber having a low energy<br />
loss, due to all causes, per unit length of fiber,<br />
usually measured in decibels/kilometer at a specified<br />
wavelength. Low-loss is usually considered to<br />
be below 20 dB/km. In low-loss fiber, attenuation<br />
of a propagating wave is caused primarily by scattering<br />
due to metal ions, by absorption due to water<br />
in the OH radical form, and by Rayleigh scattering.<br />
Low-loss fiber attenuation rates are approaching 0.01<br />
dB/km.<br />
luminous intensity. The ratio of the luminous flux<br />
emitted by a light source, or an element of the<br />
source, in an infinitesimally small cone about the<br />
given direction, to the solid angle of that cone,<br />
i.e., luminous flux emitted per unit solid angle.<br />
light-emitting diode (LED). A diode that operates sim -<br />
ilar to a laser diode, with the same total output<br />
power level, the same output limiting modulation<br />
A-II
M<br />
Mach-Zehnder interferometer. An interferometer in which<br />
an electromagnetic wave is split, each half traveling<br />
around half a loop in opposite directions, one<br />
via a beam splitter and a fixed mirror, the other<br />
via a movable mirror and a beam splitter, both halves<br />
being recombined at a photodetector where their relative<br />
phase can reinforce or cancel. The moveable<br />
mirror modulates the resultant intensity at the<br />
photodetector.<br />
magnetooptic. Pertaining to the control of lightwaves<br />
by means of magnetic fields, for example by rotating<br />
the magnetic polarization of a lightwave and thus<br />
achieving polarization modulation or by cementing<br />
or coating ferromagnetic material on the outside of<br />
a fiber and using the magnetostrictive effect to<br />
alter the length of a fiber in the sensing arm of<br />
an interferometer thus obtaining a method of converting<br />
magnetic field variations to light intensity<br />
variations. Synonymous with optomagnetic<br />
magnetooptic effect. The rotation of the polarization<br />
plane of lightwaves in a transmission medium brought<br />
about when subjecting the medium to a magnetic field<br />
(Faraday rotation). The effect can be used to modulate<br />
the light beam in a material, since many properties,<br />
such as conducting velocities, reflection<br />
and transmission coefficients at interfaces, acceptance<br />
angles, critical anglea, and transmission<br />
modes, are dependent upon the direction of propagation<br />
at interfaces in the media in which the light<br />
travels. The amount of rotation is given by:<br />
A = aHL<br />
where a is a constant, H is the magnetic field<br />
strength, and L is the propagation distance. The<br />
magnetic field is in the direction of propagation of<br />
the lightwave. Also, by coating or cementing ferroelectric<br />
material to a fiber, the magnetostrictive<br />
effect can be used to alter the length of a fiber in<br />
the sensing arm of an interferometer, thua obtaining<br />
a method of converting magnetic field variations to<br />
light intensity variationa. Synonymous with Faraday<br />
effect.<br />
magnetooptic modulator. A modulator that makes use of<br />
the magnetooptic effect to modulate a lightwave carrier.<br />
magnetostriction. The phenomenon exhibited by some<br />
materials in which dimensional changes occur when<br />
the material is subjected to a magnetic field, usually<br />
becoming longer in the direction of the applied<br />
field. The effect can be used to launch a shock or<br />
sound wave each time the field is applied or changed,<br />
possibly giving rise to phonons that could influence<br />
energy levels in the atoms of certain materials such<br />
as semiconductors and lasers and thereby serve as a<br />
modulation method. Along with photon or electric<br />
field excitation, the phonon energy could provide<br />
threshold energy to cause electron energy level<br />
transitions, causing photon absorption or emission.<br />
The effect can also be used to change the physical<br />
dimensions of an optical fiber that is wrapped<br />
around or cemented to or jacketed by, a magnetostrictive<br />
(ferromagnetic) material and thus modulate a<br />
light beam in the fiber.<br />
margin. See power margin.<br />
material dispersion. 1. The variation in the refractive<br />
index of a transmission medium as a function of<br />
wavelength, in optical transmission media used in<br />
optical waveguides; e.g., optical fibers, slab dielectric<br />
waveguides, and integrated optical circuits.<br />
Material dispersion contributes to group-<br />
-delay distortion, along with waveguide-delay distortion<br />
and multimode group-delay spread, i.e., the<br />
spreading of a pulse. 2. The part of the total<br />
dispersion of an electromagnetic pulse in a waveguide<br />
caused by the changes in properties of the<br />
material with which the waveguide, such as an optical<br />
fiber is made, due to changes in frequency. As<br />
wavelength increasea, and frequency decreases, material<br />
dispersion decreases. At high frequencies, the<br />
rapid interactions of the electromagnetic field with<br />
the waveguide material (optical fiber) renders the<br />
refractive index even more dependent upon frequency.<br />
Maxwell’s equations. A group of basic equations, in<br />
either integral or differential form, that (1) describe<br />
the relationships between the properties of<br />
electric and magnetic fields, their sources, and the<br />
behavior of these fielda at material media interfaces;<br />
(2) express the relations among electric and<br />
magnetic fields that vary in space and time in material<br />
media and free space; and (3) are fundamental to<br />
the propagation of electromagnetic waves in material<br />
media and free space. The equations are the basis<br />
for deriving the wave equation that expresses the<br />
electric and magnetic field vectors in a propagating<br />
electromagnetic wave in a transmission medium such<br />
as a lightwave in an optical fiber. Maxwell’s<br />
equations in differential form are:<br />
vx E = -aBlat<br />
v. H = J + aD/3t<br />
V. B=O<br />
V“ D=o<br />
where E, H, B, and D are the electric field intensity,<br />
the magnetic field intensity, the magnetic<br />
flux density, and the electric flux density (electric<br />
displacement) vectors, respectively, J is the<br />
electric current density, and pis the electric<br />
charge density, the v is the “del- space derivative<br />
operator, expressing differentiation with respect<br />
to all distance coordinates, the VX being the curl<br />
and the v - being the divergence. The partial derivatives<br />
are with respect to time. These equations<br />
are Used in conjunction with the constitutive relations<br />
to obtain useful practical results given actual<br />
sources of charge and current in real media.<br />
These are only valid when the field and current<br />
vectors are single-valued, bounded, continuous functions<br />
of poaition and time, and have continuous<br />
derivatives.<br />
medium. See homogeneous medium; linear medium; sourcefree<br />
medium; transmission medium.<br />
meridional ray. In an optical fiber, a light ray that<br />
passes through the central axis of the fiber, is<br />
internally reflected, and is confined to a single<br />
plane, called the meridian plane. Also see skew ray.<br />
metal oxide semiconductor. A semiconductor composed of<br />
doped metal oxide, such as silicon oxide (Si02). See<br />
combined metal oxide semiconductor.<br />
A-12
Michelson interferometer. b interferometer in which<br />
an electromagnetic wave is split. One half is then<br />
reflected from a fixed mirror and back through the<br />
splitter to a photodetector, the other half is passed<br />
directly through the splitter to a movable mirror<br />
(transducer) that reflects it back to the splitter<br />
where it is reflected to the same photodetector.<br />
The two waves can phase enhance or cancel and thus<br />
modulate the intensity at the photodetector in accordance<br />
with a baseband input signal to the movable<br />
mirror. If an optical fiber is used, the ends of<br />
the fiber form the reflecting surfaces. Moving one<br />
end with respect to the other produces the same effect<br />
as moving the mirror.<br />
microbend. A small bend or induration in the outer<br />
surface of an optical fiber core that causes lightwaves<br />
in the core to penetrate into the cladding<br />
and thus leak from the fiber. Contrast with ordinary<br />
bend.<br />
microbend loss. In an optical fiber, the loss or attenuation<br />
in signal power caused by small bends, kinks,<br />
or abrupt discontinuities in the direction of the<br />
fibers, usually caused by fiber cabling or by wrapping<br />
fibers on drums. Microbending losses usually<br />
result from a coupling or guided modes among themselves<br />
among the radiation modes when light rays<br />
enter the cladding at the microbends or get reflected<br />
at larger than critical angles and hence also enter<br />
the cladding. Use can be made of microbend loss by<br />
creating microbends in number and amplitude in accordance<br />
with a baseband signal and thus modulating<br />
leakage. Contrast with ordinary bend.<br />
microbend sensor. A transducer capable of converting<br />
mechanical mvement, such as displacement actuated<br />
by applied forces or pressures, into a modulated<br />
lightwave in an optical fiber. The microbender<br />
introduces microbends in the fiber thus modulating<br />
the lightwave intensity by causing leakage in accordance<br />
with the information-bearing baseband signal.<br />
micrometer. See micron.<br />
micron (lhn or P). A unit of length in the metric system<br />
equal to one-millionth of a meter, i.e., 10-6<br />
meter. Synonymous with micrometer.<br />
mismatch 10ss. See refractive-index-profile-mismatch<br />
loss.<br />
mixing box.<br />
See optical mixing box.<br />
mixing rod. See optical mixing rod.<br />
modal dispersion. 1. The difference in propagation<br />
time for each of the modes propagating in an optical<br />
fiber, resulting in a broadening of a light pulse.<br />
2. In the propagation of an electromagnetic wave or<br />
pulse in a waveguide, the changes introduced in the<br />
relative magnitudes of the frequency components of<br />
the wave or pulse. The guide is capable of supporting<br />
or introducing only a fixed number of frequencies<br />
depending on its geometry and material parameters,<br />
such aa permeability, permittivity, and conductivity.<br />
where a is the fiber radius, nl and n2 are the refractive<br />
indexes of core and cladding, and 1 is the<br />
wavelength. There are additional degenerate modes<br />
that can be supported, such as polarization and<br />
evanescent modes. 2. In communication systems, a<br />
form or medium for transmission of voice, image,<br />
digital data, or other signala.<br />
mode stripper.<br />
See cladding mode stripper.<br />
mode volume. For a large number of modes, N = fn2/2,<br />
where fn is the V-parameter (normalized frequency or<br />
V-value).<br />
modulation. 1. The variation of a characteristic or<br />
parameter of a wave in accordance with a characteristic<br />
or parameter of another wave. For example, a<br />
variation of the amplitude, frequency, or phase of a<br />
carrier wave in accordance with the wave form that<br />
represents information by means of superposition,<br />
mixing, or transduction. The carrier may be a continuous<br />
direct-current (DC) signal or a continuous<br />
alternating signal such as a sinusoidal wave. The<br />
carrier is used as a means of propagation. The<br />
superimposed or mixed aignal is used as the intelligence-bearing<br />
signal. The variation of the modulated<br />
carrier is detected at the receiver. The information<br />
or intelligence frequencies are normally called<br />
the baseband. 2. In fiberoptic, the variation<br />
of a characteristic or parameter of a lightwave in<br />
order to superimpose an information-bearing signal<br />
on a carrier wave. For example, a variat~on of the<br />
amplitude, frequency, or phase of a lightwave by an<br />
analog or digital baseband signal in a fiberoptic<br />
sensor, transmitted in an optical fiber, and recovered<br />
by a photodetector. The carrier may be a continuous<br />
lightwave when it is not modulated by the sensor.<br />
Contrast with demodulation. See amplitude<br />
modulation; phase modulation; polarization modulation;<br />
frequency modulation.<br />
modulator. A device that accomplishes modulation, that<br />
is, has the capability of varying one signal in accordance<br />
with the variations of another aignal. Thus,<br />
it converts baseband signal into a modulated carrier.<br />
moving grating sensor. A sensor consisting of a fixed<br />
and moveable grating of transparent and opaque areas<br />
such that the intensity of light passing through is<br />
modulated according to the amount that the transparent<br />
areas of both gratings coincide (overlap) aa<br />
the movable grating is moved according to the applied<br />
baseband aignal.<br />
multimode fiber. An optical fiber waveguide that will<br />
allow (support) more than one mode to propagate.<br />
Multimode optical fibers have a much larger core (25<br />
to 75 microns) than aingle-mode fibers (2 to 12<br />
microns diameter) and thus permit nonaxial rays or<br />
modes to propagate through the core.<br />
multiplexing. See frequency-division multiplexing; polarization<br />
multiplexing; space-division multiplexing;<br />
time-division multiplexing (TDM); wavelengthdivision<br />
multiplexing (WDM).<br />
mode. 1. A specific condition or arrangement of electromagnetic<br />
waves in a transmission medium, particularly<br />
in a waveguide. The total number of dimensional<br />
modes that a step-index optical fiber can support,<br />
couple to, or radiate into is given by:<br />
1= ~2a2 (n12-n22)/A2<br />
A-13
N<br />
nanometer. One thousandth of a micron, i.e. , 10-9<br />
met er.<br />
near total internal reflection sensor. In fiberoptic,<br />
a fiberoptic sensor that operates on the principle<br />
of varying the property of an optical fiber in such<br />
a manner that the amount of light that leaks into<br />
the cladding ie altered by varying the critical angle<br />
in accordance with a baseband signal, auch as by<br />
altering the refractive index or the ordinary bend<br />
radius, thus altering the internal reflection.<br />
noise. In a fiberoptic system, the sum of unwanted or<br />
disturbing energy introduced into the system from<br />
natural or man-made sources, such as unwanted lightwaves<br />
coupled into an optical fiber or unwanted modulation<br />
of lightwaves in an optical fiber due to environmental<br />
conditions that alter the propagation or<br />
modulation characteristics of an optical fiber or<br />
fiberoptic sensor.<br />
noise power. The power that is developed by unwanted<br />
electromagnetic waves from all sources in the output<br />
of a device, such as a transmission channel or amplifier.<br />
Noise power is usually the total noise power<br />
of waves with frequencies within the passband of the<br />
system or device. Croastalk, distortion, and lntermodulation<br />
products are usually classed as noise.<br />
normalized frequency.<br />
See V-parameter.<br />
numerical aperture (N.A.). A measure of the light-accepting<br />
property of an optical fiber. For example,<br />
glass; given by:<br />
N.A. = (n12-n22)1/2<br />
i.e., the square root of the difference of the<br />
squares of the refractive indices of the core, nl,<br />
and the cladding, n2. If nl is 1.414 (glass) and n2<br />
is 1.0 (air), the numerical aperture is 1.0 and all<br />
incident rays will be trapped. The numerical aperture<br />
is a measure of the characteristic of an optical<br />
waveguide in terms of its acceptance of impinging<br />
light. The degree of openness, light-gathering<br />
ability, angular acceptance, and acceptance cone are<br />
all terms describing the characteristic. It may be<br />
necesaary to specify that the refractive indices are<br />
for step index fibera and for graded index fibers;<br />
nl is the maximum index in the core and n2 is the<br />
minimum Indexin the cladding. As a number, theN.A.<br />
expresses the Mghtgathering power of a fiber. It<br />
is mathematically equal to the sine of the acceptance<br />
angle. A method of meaauring the N.A. is to excite<br />
the fiber in the visible region and display the light<br />
emerging from the end perpendicularly on a screen<br />
about 10 to 30 cm away. The measured diameter of<br />
the projected circle of light divided by twice the<br />
distance from the fiber end to the screen is the<br />
numerical aperture. The numerical aperture is also<br />
equal to the sine of the half-angle of the widest<br />
bundle of rays capable of entering a lens, multiplied<br />
by the refractive index of the medium containing<br />
that bundle of rays, i.e., the incident medium.<br />
Typical numerical apertures for plastic-clad fused<br />
silica optical fibers range from 0.25 to 0.45.<br />
optic.<br />
optical cable.<br />
See fiberoptic.<br />
optical circuit.<br />
optical data link.<br />
0<br />
See fiberoptic cable.<br />
See integrated optical circuit.<br />
See fiberoptic data link.<br />
optical fiber. A single discrete optical transmission<br />
element or waveguide usually consisting of a fiber<br />
core and a fiber cladding that can guide a lightwave<br />
and is usually cylindrical in shape. It consists<br />
either of a cylinder of transparent dielectric material<br />
of a given refractive index whose walls are in<br />
contact with a second dielectric material of a lower<br />
refractive index; or of a cylinder whose core has a<br />
refractive index that gets progressively lower away<br />
from the center. The length of a fiber is usually<br />
much greater than its diameter. The fiber relies<br />
upon internal reflection to transmit light along its<br />
axial length. Light enters one end of the fiber and<br />
emerges from the opposite end with losses dependent<br />
upon length, absorption, scattering, and other factors.<br />
A lightwave in an optical fiber can be modulated<br />
by changing the light propagation parameters<br />
of the fiber. A bundle of fibers has the ability<br />
to transmit a picture from one of its surfaces to<br />
another, around curves, and into otherwise inaccessible<br />
places with an extremely low losa of definition<br />
and light, by the proceas of total internal reflection.<br />
One optical fiber classification scheme is<br />
to divide them into plastic, glaas, or plastic-clad<br />
fuaed silica fibers; then into step-index multimode,<br />
graded-index multimode, or step-index single mode<br />
fibers. Plastic is less brittle than glass but has<br />
increased attenuation compared to glass. Synonymous<br />
with light pipe. See self-focusing optical fiber.<br />
optical fiber coating. A protective material bonded to<br />
an optical fiber over the cladding to preserve fiber<br />
atrength and inhibit cabling losses by providing protection<br />
againat mechanical damage, protection against<br />
moisture and debilitating environments, compatibility<br />
with fiber and cable manufacture, and compatibility<br />
with the jacketing proceas. Coatings include<br />
fluorpolymers, Teflonc, Kynarc, polyurethane,<br />
and many others. Application methods include dipcoating<br />
(for those in solution), extrusion, spray<br />
coating, and electrostatic coating.<br />
optical fiber jacket. A material used to cover an optical<br />
fiber, whether or not it is cladded or coated.<br />
optical fiber loss. The optical power loss in an optical<br />
fiber, usually expressed in dB/km.<br />
optical fiber preform. Specially-shaped material from<br />
which an optical fiber is made, usually by drawing<br />
or rolling. For example, a solid glass rod made with<br />
a higher refractive index than the tube into which<br />
it is alipped,<br />
into a cladded optical fiber; or<br />
tive-index rods surrounding a<br />
index rod heated and drawn into a<br />
drawing procesa results in fiber<br />
than the preforma.<br />
to be heated and drawn or rolled<br />
four lower-refrachigher-refractivecladded<br />
fiber. The<br />
many times longer<br />
A-14
optical fiber ribbon. A rowof optical fibers laminated<br />
in a flat plastic strip. Synonymous with fiberoptic<br />
ribbon.<br />
optical fiber sensor.<br />
Synonym for fiberoptic sensor.<br />
optical integrated circuit. A synonym for integrated<br />
optical circuit.<br />
optical mixing box. A fiberoptic coupler consisting of<br />
a piece of fiberoptic material that receives several<br />
optical frequencies and that mixes them to produce<br />
dichromatic or polychrometic lightwaves for dispatch<br />
via one or more outputs for transmission elsewhere<br />
and perhaps subsequent separation into the constituent<br />
frequencies to produce the original information<br />
introduced by the modulation of each of the constituent<br />
frequencies. The mixing box usually has reflective<br />
inner surfaces, except at the ports. The<br />
lightwaves entering the box are usually a group of<br />
monochromatic waves each of a different frequency<br />
and each modulated separately.<br />
optical mixing rod. An optical mixing box that has the<br />
general shape of a right circular cylinder, usually<br />
with pigtails to serve as entrance and exit ports.<br />
optical power budget. In an optical transmission system,<br />
the distribution of the available power that is<br />
required for transmission within specified distortion<br />
limits or error rates. The distribution is<br />
usually in terms of decibels for each component of<br />
the system from source to sink. Components include<br />
the light source pigtail, connectors, cable, splices,<br />
and detector pigtail.<br />
optical power density. The optical energy per unit time<br />
transmitted by a light beam through a unit area normal<br />
to the direction of propagation or the direction<br />
of maximum power gradient, expressed in watts per<br />
square meter or joules per second-(square meter).<br />
A watt is a J/S.<br />
optical power efficiency. The ratio of the emitted<br />
electromagnetic power of an optical source to the<br />
electrical input power to the aource.<br />
optical repeater. An optical/optical, optical/electrical,<br />
or electricalloptical signal amplification and<br />
processing device. The repeater usually accepts an<br />
optical signal, converts it into an electrical signal<br />
(photodetection) amplifies it, and converts it<br />
back to an optical signal for further transmission.<br />
optical sensor.<br />
See slab dielectric optical wave-<br />
optical waveguide.<br />
guide.<br />
optics.<br />
optoacoustics.<br />
See fiberoptic sensor.<br />
See integrated optics.<br />
Synonym for acoustooptics.<br />
optoelectronic. 1. Pertaining to the conversion of<br />
optical power or energy into electrical power or<br />
energy, such as the conversion of an optical signal<br />
into an electrical signal. Also see electrooptic.<br />
2. Synonym for electrooptic.<br />
optoelectronic device.<br />
optomagnetic. See magnetooptic.<br />
See electrooptic device,<br />
optostrain. Pertaining to the change in lightwave propagation<br />
characteristics caused by changes in waveguide<br />
parameters due to strain resulting from applied<br />
stress (tensile, compression, shear, bending,<br />
torsional or combinational stress). Synonymous with<br />
optostress.<br />
optostress. A synonym for optostrain.<br />
ordinary bend. A bend in the core of an optical fiber<br />
in which the central axis of the core may be said to<br />
have a bend with finite nonzero radius. If the<br />
radius of the bend is smaller than the critical<br />
radius, light will leak from the core as total internal<br />
reflection no longer takes place. Bending a<br />
fiber from more than to less than the critical<br />
radius can be used to modulate the light intensity<br />
or the leakage. Contrast with microbend.<br />
See combined metal oxide semicon-<br />
oxide semiconductor.<br />
ductor.<br />
parameter.<br />
— PD.<br />
P<br />
See refractive index profile parameter.<br />
See photodetector.<br />
phase detection. Obtaining an output electrical signal<br />
proportional to an input lightwave phase angle that<br />
varies with respect to a fixed reference in accordance<br />
with a baseband input signal. Often phase detection<br />
can be accomplished by conversion to amplitude<br />
detection.<br />
?hase-lock loop. An electronic circuit that controls<br />
an oscillator so that it maintains a constant phase<br />
angle relative to a reference signal source. The<br />
system can be used in situations in which signals<br />
that are shifted in phase with respect to one another<br />
maintain a fixed or specified phase relationship.<br />
In spread-spectrum systems a phase-lock loop<br />
is used to cause an oscillator internal to the feedback<br />
loop to oscillate at an incoming carrier frequency.<br />
The feedback, or servoloop, circuit utilizes<br />
the output of a phase-sensitive detector, via a<br />
low pass filter, to control the frequency of its own<br />
reference signal. The feedback loop is damped to<br />
permit tracking of the carrier phase changes at the<br />
input, but not tracking of the modulation changes.<br />
The arrangement also provides a low noise threshold.<br />
In fiberoptic systems, a similar arrangement can<br />
be used to control the phase of a continuous or modulated<br />
lightwave carrier.<br />
phase modulation (PM). Angle modulation in which the<br />
instantaneous phase angle of an unmodulated sine<br />
wave carrier is varied proportionally in accordance<br />
with the instantaneous value of the amplitude of a<br />
modulating signal.<br />
phase velocity. The velocity with which a specific<br />
point on a sine wave (e.g., the peak value of the<br />
electric vector of an electromagnetic wave) is propagated<br />
in a material medium or in free space. This<br />
concept can only strictly be applied to a single<br />
frequency wave, such as an unmodulated carrier wave.<br />
The phase velocity is the propagation velocity of a<br />
uniform plane sinusoidal wave, given as the wavelength<br />
times the frequency of the wave. The phase<br />
A-15
velocity is also the velocity at which an observer<br />
would have to move to make the wave characteristics<br />
appear to remain constant in phase in a given medium.<br />
The phase velocity in a given medium is equal<br />
to the velocity of propagation of the wave divided<br />
by the refractive index of the medium when the wave<br />
is an electromagnetic wave. It is not the velocity<br />
of electromagnetic energy propagation, although it<br />
may be higher than the velocity of light in free<br />
space. For a given frequency, the wavelength is less<br />
in material media than in free space when electromagnetic<br />
waves are involved. In nondispersive media,<br />
the phase velocity and the group velocity are equal.<br />
Also see group velocity.<br />
photodetector (PD). A device that is capable of extracting<br />
information from a lightwave by producing<br />
an electrical output signal from an optical input<br />
signal.<br />
yhoton. A quantum of electromagnetic energy. The<br />
energy of a photon is hf, where h is Planck’s constant,<br />
and f is the frequency of the radiation.<br />
ylane of polarization.<br />
See polarization plane.<br />
p-n junction. In a semiconductor (solid-state) device,<br />
the interface between semiconducting ~terial that<br />
has been doped positively, i.e., with an impurity<br />
material that produces holes (acceptor sites) on one<br />
side of the interface, and material that produces<br />
relatively free electrons (donor sites) on the other<br />
side. The junction is usually assumed to be abrupt,<br />
or linearly graded in its transition region across<br />
the interface.<br />
Pockel cell. A material, usually a crystal, whose refractive<br />
index change is linearly proportional to a<br />
change in an applied electric field, the material<br />
being configured so as to be part of another system,<br />
such as an optical path. The cell thus provides a<br />
means of modulating the light in the optical path.<br />
polarimetric sensor. In fiberoptic, a sensor in which<br />
a baseband input signal alters the polarization of a<br />
lightwave in an optical fiber or the output intensity<br />
is varied by a process of polarization selection.<br />
polarization. The direction of the electric field vector<br />
of an electromagnetic wave, such as a lightwave.<br />
It is the property of a radiated electromagnetic<br />
wave that describes the time-varying direction and<br />
amplitude of the electric field vector, that, together<br />
with the magnetic field vector, makes up the<br />
wave. It is specifically illustrated by the figure<br />
that is traced in space as a function of time by<br />
the extremity (tip) of the vector that represents<br />
the electric field with its base at a fixed point in<br />
space, as observed along the direction of propagation.<br />
In general, for a plane polarized wave, the<br />
figure is elliptical and it is traced in a clockwise<br />
or counterclockwise sense. Circular polarization<br />
and linear polarization are obtained when the ellipse<br />
becomes a circle or a straight line, respectively.<br />
Clockwise sense rotation of the electric field vector<br />
is designated right-hand polarization, and counterclockwise<br />
sense rotation is designated left-hand<br />
polarization. Sense of rotation is obtained by viewing<br />
the rotating electric field vector while facing<br />
in the direction of propagation. The direction of<br />
propagation is the forward direction of a right-hand<br />
screw obtained when the electric vector is rotated<br />
through the smaller angle into the magnetic vector,<br />
A-16<br />
the direction of propagation being perpendicular<br />
to both fields, namely, the direction of the Poynting<br />
vector.<br />
polarization diversity. 1. Pertaining to the ability<br />
to change the direction of polarization of an electromagnetic<br />
wave, usually at the source of radiation,<br />
by changing the direction of the polarization<br />
plane, the horizontal or vertical polarization, i.e.,<br />
the polarization angle with respect to a fixed reference<br />
or the linear, circular, elliptical, or helical<br />
polarization. 2. Pertaining to two or more types<br />
of polarization. 3. Any method of diversity transmission<br />
and reception in which the same information<br />
signal is transmitted and received simultaneously<br />
on orthogonally polarized waves with fade-independent<br />
propagation characteristics. Also see diversity<br />
reception.<br />
polarization modulation. The modulation of an electromagnetic<br />
wave in such a manner that the polarization<br />
of the carier wave, such as the direction of polarization<br />
of the electric and magnetic fields, or their<br />
relative phasing, to produce changes in polarization<br />
angle in linear, circular, or elliptical polarization,<br />
is varied according to a characteristic of an<br />
information-bearing input signal, such as a pulseor-no-pulse<br />
digital signal. In optical fibers or<br />
other waveguides, polarization shifts that are made<br />
in accordance with an input signal variation are a<br />
practical means of modulation.<br />
polarization multiplexing. Multiplexing accomplished by<br />
using two mor more lightwave polarization modes in<br />
the same transmission medium at the same time with<br />
the same frequency. Each polarization mode would<br />
constitute a separate channel.<br />
polarization plane. In a transverse, or ordinary, electromagnetic<br />
(TEM) wave, the plane defined by the<br />
electric and magnetic field vectors of the wave;<br />
i.e., both field vectors at a point lie in, and<br />
therefore define, the polarization plane. The direction<br />
of propagation, or power flow, of the wave<br />
is perpendicular to both the electric and magnetic<br />
field vectors at the point, i.e., perpendicular to<br />
the polarization plane at that point. The wavefront<br />
lies in the polarization plane. The Poynting vector,<br />
ExH, is perpendicular to the polarization plane.<br />
polarized light. A light beam whose electric vector<br />
vibrates in a direction that doea not change, unless<br />
the propagation direction changes; i.e., it is in a<br />
plane perpendicular to the direction of propagation.<br />
If the time-varying electric vector can be broken<br />
into two perpendicular components that have equal<br />
amplitude and that differ in phase by 1/4 wavelength,<br />
the light is said to be circularly polarized.<br />
Circular polarization is obtained whenever<br />
the phaae difference between the two perpendicular<br />
components is any odd, integral number of quarter<br />
wavelengths. If the electric vector is resolvable<br />
into two perpendicular components of unlike amplitudes<br />
and differing in phase by values other than<br />
O, 1/4, 1/2, 3/4, 1, etc., wavelengths, the light<br />
beam is said to be elliptically polarized.<br />
population inversion. A redistribution of energy levels<br />
in a population of elements such that, instead of<br />
having more atoms with lower-energy-level electrona,<br />
there are fewer atoms with higher-energy-level electrona.<br />
That ia, an increaae in the total number of<br />
electrons in the higher excited states occurs at<br />
the expense of the energy in the electrons in the
ground or lower state and at the expense of the<br />
resonant energy source (i.e. , the pump). This is<br />
not an equilibrium condition. It is forced and must<br />
be maintained, i.e, stimulated. The generation of<br />
population inversion is caused by pumping. When<br />
electrons revert to their lower levels, photons are<br />
emitted obtaining laser action. In a stimulated<br />
material, such as a semiconductor, the upper energy<br />
level of two possible electronic energy levels in a<br />
given atom, distribution of atoms, molecule, or distribution<br />
of molecules, has a higher probability<br />
(usually only slightly higher) of being occupied by<br />
an electron. When population inversion occurs, the<br />
probability of downward energy transition giving<br />
rise to radiation, is greater than the probability<br />
of upward energy transitions, giving rise to photon<br />
absorption, resulting in a net radiation level, thus<br />
obtaining stimulated emission, i.e., laser action.<br />
=“<br />
See transmitted power.<br />
power budget. The allocation of available power in a<br />
system to the various functions that need to be performed.<br />
For example, in a fiberoptic data link, the<br />
distribution of available optical power among all<br />
the elements of the link, such as couplers, splices,<br />
fibers, and pigtails; or in a satellite communication<br />
system, the distribution of the available power<br />
in a satellite for maintaining orientation, maintaining<br />
orbit control, and for the reception and retransmission<br />
of signals. See optical power budget.<br />
power density.<br />
See optical power density.<br />
power margin. An extra amount of power that may be<br />
specified by a designer because of uncertainties in<br />
the empirical design method, loss, characteristics,<br />
material variability, and variation in equipment performance<br />
parameters and characteristics. For example,<br />
in an optical power budget, the optical power,<br />
PM, that remains after subtracting the sum of all<br />
the optical losses, PL, and the power input required<br />
by a photodetector, PR, from the available optical<br />
power output by a source, P5, i.e.,<br />
profile.<br />
pM = ps<br />
- [pL+pR].<br />
See radial refractive index profile.<br />
profile mlsmstch loss.<br />
mismatch loss.<br />
profile parameter.<br />
parameter.<br />
*“<br />
See refractive-index-profile<br />
See refractive index profile<br />
See electromagnetic pulse (EMP).<br />
punch-through voltage. In a semiconductor junction, a<br />
voltage equal to that required to just overcome the<br />
potential barrier of the junction to permit the flow<br />
of electrons that are in the conduction band.<br />
R<br />
radial refractive-index profile. In an optical fiber<br />
with a circular cross section, the refractive index<br />
described as a function of the radial distance from<br />
the center. For example, the function:<br />
n=n~ f(r)<br />
where n is the refractive index at a radial distance<br />
r from the center, nl is the refractive index at the<br />
center, and f(r) is the function of r that expresses<br />
the index at the distance r from the center , usually<br />
independent of radial direction. Also see refractive<br />
index profile parameter.<br />
radiation. See light amplification by stimulated emission<br />
of radiation (laser).<br />
~. See light ray; meridional ray; reflected ray;<br />
skew ray.<br />
Rayleigh scattering. The scattering of lightwaves propagating<br />
in material media due to the atomic or molecular<br />
structure of the material and variations in<br />
the structure as a function of distance. The scattering<br />
losses vary as the reciprocal of the fourth<br />
power of the wavelength. The distances between<br />
scattering centers must be small compared to the<br />
wavelength. Rayleigh scattering sets a theoretical<br />
lower limit to the attenuation of a propagating<br />
lightwave as a function of wavelength, ranging from<br />
10 dB/km at 0.50 micron to 1 dB/km at 0.95 micron.<br />
Material scattering is caused primarily by Rayleigh<br />
scattering. Rayleigh scattering is also due to the<br />
variation in molecular density of intrinsic material;<br />
for example, the familiar light green color of<br />
pop bottles is due to Rayleigh scattering from distributed<br />
iron atoms. This represents the limiting<br />
absorption. Also since it decreases with A, this<br />
has resulted in using higher wavelengths to achieve<br />
low-loss fiber. Minimum attenuation is due to decreases<br />
in absorption due to Rayleigh scattering<br />
and increases due to OH- vibration. Also see scattering.<br />
ray trapping. Preventing a lightwave from leaking from<br />
a waveguide. For example, total internal reflection<br />
causes ray trapping.<br />
recombination.<br />
See electron-hole recombination.<br />
reflected ray. A ray of electromagnetic radiation,<br />
usually light leaving a reflecting surface. The ray<br />
Indicates the path after reflection.<br />
reflection. When electromagnetic waves, such as light<br />
rays, strike a smooth, polished surface, their return<br />
or bending back into the medium from whence<br />
they came. Specular or regular reflection from a<br />
polished surface, such as a mirror, will return a<br />
major portion of the light in a definite direction<br />
lying in the plane of the incident ray and the normal.<br />
After specular reflection, light can be made<br />
to form a sharp image of the original source. Diffuse<br />
reflection occurs when the surface is rough and<br />
the reflected light is scattered from each point in<br />
the surface. These diffuse rays cannot be made to<br />
form an image of the original source, but only of<br />
the diffusely reflecting surface itself. Also see<br />
Snell’s law; internal reflection; total internal<br />
reflection.<br />
reflection coefficient. 1. The ratio of the reflected<br />
field strength to the incident field strength when<br />
an electromagnetic wave is incident upon an interface<br />
surface between dielectric media of different<br />
refractive indices. If, at oblique incidence, the<br />
magnetic field component of the incident wave is<br />
parallel to the interface, the reflection coefficient<br />
is given by:<br />
A-17<br />
R = (nlcosA -<br />
n2cosB)/(nlcosA + n2cosB)
where nl and n2 are the reciprocals of the refractive<br />
indices of the incident and transmitted mediums,<br />
respectively, and A and B are the angles of<br />
incidence and refraction (with respect to normal),<br />
respectively. If, at oblique incidence, the electric<br />
field component of the incident wave is parallel<br />
to the interface, the reflection coefficient is<br />
given by:<br />
R = (n2cosA -<br />
nlcosB)/(n2cosA + n~cosB)<br />
These equations are known as the Fresnel equations<br />
for such cases. For large smooth surfaces, the reflection<br />
coefficient may be near unity, such as for<br />
highly polished mirrors. At near grazing incidence<br />
angles, that is nearly 90° from the normal to the<br />
surface, even rough surfaces may reflect relatively<br />
well, i.e., total reflection occurs. 2. At any<br />
specified point in a transmission line between a<br />
power source and a power sink (absorber), the vector<br />
ratio of the electric field associated with the reflected<br />
wave to that associated with the incident<br />
wave. The reflection coefficient, RC, is given by<br />
RC = (Z2-Zl)/(Z2+Zl) = (SWR-1)/(SWR+l),<br />
where Z1 iS the impedance looking toward the source,<br />
Z2 is the impedance looking toward the load, and SWR<br />
ia the standing wave ratio. Also see transmission<br />
coefficient.<br />
reflection sensor.<br />
sensor.<br />
See near total internal reflection<br />
reflective star-coupler. An optical-fiber coupling device<br />
that enables signals in one or more fibers to<br />
be transmitted to one or more other fibers by entering<br />
the signals into one side of an optical cylinder,<br />
fiber, or other piece of material, with a reflecting<br />
back-surface in order to reflect the diffused<br />
signals back to the output ports on the same<br />
aide of the material, for conduction away in one or<br />
more fibers.<br />
refraction. The bending of oblique (non-normal) incident<br />
electromagnetic waves or raya as they cross the<br />
interface between a transmission medium of one refractive<br />
index into a medium of a different refractive<br />
index. The velocityof propagationof theelectromagnetic<br />
waves change when passing from a medium<br />
to one with a different refractive index. Also see<br />
Snell’s law<br />
refraction angle. When an electromagnetic wave strikes<br />
an interface surface between media with different<br />
refractive indices and is wholly or partially transmitted<br />
into the new medium, the acute angle between<br />
the normal to the surface at the point of incidence<br />
and the refracted ray.<br />
refractive index. 1. The ratio of the velocity of<br />
light in a vacuum to the velocity of a given frequency<br />
of light in the transmission medium whose refractive<br />
index is desired; e.g., n = 2.6 for certain<br />
kinds of glass. 2. The ratio of the sines of the<br />
incidence angle and the refraction angle when light<br />
passes from one medium to another. The index between<br />
two media ia the relative index, while the<br />
index when the first medium is a vacuum is the absolute<br />
index of the second medium. The refractive<br />
index expressed in tables is the abaolute index,<br />
i.e., vacuum-to-substance at a certain temperature,<br />
with light of a certain frequency. Examples: vacuum,<br />
1.000; air, 1.000292; water, 1.33; ordinary crown<br />
glass, 1.516. Since the index of air is very cloae<br />
to that of vacuum, the two are often used interchangeably.<br />
The refractive index of a substance<br />
is given as:<br />
where p is the magnetic permeability of the substance,<br />
E ia the electric permittivity, P. is the<br />
magnetic permeability of a vacuum, and E. is the<br />
electric permittivity of a vacuum, although nearly<br />
the same relative to air.<br />
refractive index profile.<br />
profile.<br />
See radial refractive index<br />
refractive-index-profile mismatch loss. A 10SS Of Sig -<br />
nal power that occurs when two optical fibers are<br />
butt-coupled and their refractive index profiles are<br />
not the same.<br />
refractive index profile parameters. The exponent i in<br />
the relation that expresaes the refractive index as<br />
a function of the radial diatance from the central<br />
axis of an circular optical fiber, i.e., in the<br />
expression:<br />
nfnl =<br />
[1-(r/a)i]l/2<br />
where n is the refractive index at the radial distance<br />
r and a is the radiua of the fiber core. For<br />
a step-index fiber i= co for ra; for<br />
a parabolic graded-index fiber, i=2. A value of i=<br />
2.25 will minimize or eliminate intermodal dispersion<br />
and maximum the length-bandwidth product.<br />
rejection ratio. See common-mode rejection ratio<br />
(CMRR).<br />
~. A bounded region in a material medium,<br />
such as a free rectangular space in a laser<br />
crystal, a length of metal hollow tubing closed on<br />
both ends, a short length of optical fiber with mirrors<br />
on both ends, or the reflection could be due to<br />
a 3-dB coupler or a splice associated with the insertion<br />
loss, or a region of such geometrical dimension,<br />
such as two parallel walls that are a multiple<br />
or submultiple of wavelengths apart, that a standing<br />
wave (electromagnetic, acoustic, or elastic) can<br />
be austained and raised to high intensity by application<br />
of stimulation (applied energy of appropriate<br />
frequency) from outside or inside the cavity. Resonant<br />
cavities are used in some lasers in which they<br />
form part of the laser head.<br />
ribbon.<br />
See optical fiber ribbon.<br />
risetime. In pulse circuits, the time required for a<br />
pulse to reach a specific magnitude from a given<br />
level. For example, the time required for a voltage<br />
or a light pulse to change from 0.1 to 0.9 of its<br />
maximum value.<br />
risetime budget. In fiberoptic transmission systems,<br />
an accounting of all the riaetimea (time required<br />
for a lightpulse to reach a apecified level) in a<br />
aequence of optical and electrical components. Because<br />
the distribution of photon energies in lightwaves<br />
are Gausaian, the risetimes of a aequence of<br />
components are combined as the aquare root of the<br />
sum of the squarea of the individual ristimes.<br />
A-18
s<br />
Sagnac interferometer. An interferometer in which a<br />
lightwave is split and passed in opposite directions<br />
around the same rigid rotating loop by means of mirrors<br />
to a single photodetector. The phase cancellation<br />
and enhancement, and hence light intensity at<br />
the photodetector, will vary as the angular velocity<br />
is varied, thus obtaining a measure of angular acceleration.<br />
scatter. The process in which the direction, frequency,<br />
phase, or polarization of sound or electromagnetic<br />
waves is changed when the waves encounter one<br />
or more discontinuities in the transmission medium<br />
that have lengths of the order of a wavelength.<br />
Scattering usually implies a random or disordered<br />
change or distribution in the incident energy.<br />
scattering. The deflection of electromagnetic waves<br />
caused by movement of free and bound charges (e.g.,<br />
electrons, protons, and ions) in a transmission<br />
medium, the scattered fields being created as a result<br />
of the movement. The scattered field and the<br />
incident field define the total field. See Rayleigh<br />
scattering.<br />
sm. See space-division multiplexing.<br />
—<br />
self-focusing optical fiber. ATI optical fiber that is<br />
capable of focusing lightwaves by precision-control<br />
of geometry, refractive indices, light wavelength,<br />
and other parameters. The fiber is frequency-selective.<br />
SELFOC fiber. Self-focusing optical fiber produced by<br />
Nippon Electric Company and Nihon Sheet Glass Company.<br />
semiconductor. A material, such as diamond, silicon,<br />
galium-arsenide, germanium, gray tin, tellurium, and<br />
selenium, that has a filled valence-electron energy<br />
band separated by a finite band-gap energy from a<br />
higher-energy conduction band. Thus, semiconductors<br />
are neither insulators, with large band gaps and<br />
small electronic nobilities, nor metallic conductors<br />
with extremely high conductivities. Semiconductors<br />
possess covalent bonding wherein electron pairs are<br />
held tightly in the region between adjacent atoms or<br />
ions. The band-gap energy is the energy required to<br />
break an electron out of one of theae bonds. Semiconductors<br />
are often grown in single crystals and<br />
sliced or cut, to form diodes, transistors, lasers,<br />
and LEDS, thus preserving an ordered crystal lattice<br />
structure suitable for accepting positive or negative<br />
dopants. See combined metal oxide semiconductor;<br />
metal oxide semiconductor.<br />
sensor. A device or means to extend the natural senses.<br />
For example, equipment that detects or indicates<br />
terrain configuration or that detects the presence<br />
of objects or their motion by means of energy<br />
that is emitted or reflected by the objects; equipment<br />
that detects physical variables, such as temperature,<br />
pressure, humidity, weight, vibration, or<br />
acceleration; equipment that detects the presence or<br />
intensity of illumination, radio waves, ionization<br />
density, electric fields, or magnetic fields; or<br />
equipment that detects the presence of chemicals,<br />
such as pollutants and irritants; or the presence of<br />
radioactivity. Most detectors are in fact transducers,<br />
since they convert energy to another form<br />
and amplify it. They are usually designed to meas–<br />
ure variations in the quantities that they are sensing.<br />
A fiberoptic sensor makes use of changes in<br />
its light propagation properties to detect and measure<br />
the environmental changes it is subjected to.<br />
See brightfield sensor; fiberoptic sensor; darkfield<br />
sensor; interferometric sensor; intensity sensor;<br />
microbend sensor; near total internal reflection<br />
sensor; polarimetric sensor.<br />
sensor array. A spatial distribution of sensors. The<br />
spatial distribution may be used to obtain baseband<br />
directional information and to achieve various forms<br />
of multiplexing.<br />
sheath.<br />
See fiberoptic sheath.<br />
signal. 1. A time-dependent value attached to a transient<br />
physical phenomenon used to convey data, e.g.,<br />
the variation of light intensity at a point in an<br />
optical waveguide to represent a binary digit, the<br />
light-level change propagating as a pulse along the<br />
guide. 2. An impulse, either electrical, as in a<br />
wire; acoustic, as used in aonar; or a short burst<br />
of light energy, as generated by a laser and coupled<br />
to an optical fiber for guidance and transmission<br />
and for conversion back to an electrical pulse at<br />
the far end of the fiber.<br />
signal processing. The transformation of an input signal,<br />
i.e., a specific wave shape, into some other<br />
desirable form or other wave shape, usually by means<br />
of particular electronic circuits, lens systems,<br />
waveguides, antennae, or other circuit elements,<br />
such as detectors, rectifiers, pulse compressors,<br />
pulse expanders, pulse generators, nonlinear circuits,<br />
or gates. It includes the detection, shaping,<br />
converting, coding, or time positioning of an<br />
electrical, electromagnetic, or acoustic signal.<br />
single heterojunction. In a laser diode, a single junction<br />
involving two energy level shifts and two refractive<br />
index shifts, used to provide increased confinement<br />
of radiation direction, improved control of<br />
radiative recombination, and reduced nonradiative<br />
(thermal) recombination. Synonymous with close-confinement<br />
junction.<br />
single-mode fiber. An optical fiber that supports the<br />
propagation of only one mode. Usually a low-loss<br />
optical waveguide with a very small core (2 to 12<br />
microns diameter). It requires a laser source for<br />
the input signals because of the very small entrance<br />
aperture (acceptance cone) and the narrow spectral<br />
width. The small core radius approaches the wavelength<br />
of the source, consequently only a single<br />
mode is generated and propagated.<br />
skew ray. In an optical fiber, a light ray that is not<br />
confined to a plane, does not pass through the optical<br />
axis, is not parallel to the optical axis, and<br />
yet is totally internally reflected, thus taking a<br />
curling (corkscrew) path. In certain graded index<br />
fibers, the skew ray travels in a helical path along<br />
the fiber never intersecting the optical axis, particularly<br />
as long as the fiber is straight. It is<br />
not confined to the meridian plane or any other<br />
plane, nor is it a meridional ray. Also see meridional<br />
ray.<br />
A-19
slab dielectric optical waveguide. An optical waveguide<br />
consisting of rectangular layers or ribbons<br />
of materials of differing refractive indices that<br />
support one or more lightwave transmission modes,<br />
with the energy of the transmitted waves confined<br />
primarily to the layer of highest refractive index,<br />
the lower indexed medium serving aa cladding, jacketing,<br />
or surrounding medium. Slab dielectric optical<br />
waveguides are used in integrated optical circuits<br />
for geometrical convenience, in contrast to<br />
the optical fibers in cables for long-distance<br />
transmission.<br />
slab dielectric waveguide. An electromagnetic waveguide<br />
consisting of a dielectric transmission medium<br />
of rectangular cross section. The width and thickness<br />
of the guide may be controlled to support<br />
specific propagation modes; it may be cladded, protected,<br />
distributed, and electronically controllable;<br />
and it may be mounted on integrated electrooptical<br />
circuit substrate.<br />
Snell’s law. When electromagnetic wavea, such as light,<br />
pass from a given transmission medium to a medium<br />
of higher refractive index (denser) medium, its path<br />
is deviated toward the normal. When paasing into<br />
a less dense medium, its path is deviated away from<br />
the normal. Often called the law of refraction,<br />
Snell’s law defines this phenomenon<br />
the relation between the incidence<br />
by describing<br />
angle and the<br />
refraction angle as follows:<br />
sin@l/sine2 = n2/nl<br />
where 81 is the incidence angle, ’32 is the refraction<br />
angle, n2 is the refractive index of the medium<br />
containing the refracted ray, and nl is the refractive<br />
index of the medium containing the incident<br />
ray. Stated in another way, both laws, that of reflection<br />
and of refraction, are attributed to Snell,<br />
namely, when the incident ray, the normal to the<br />
surface at the point of incidence of the ray on the<br />
surface, the reflected ray, and the refracted ray<br />
all lie in a single plane, the angle between the incident<br />
ray and the normal is equal in magnitude to<br />
the angle between the reflected ray and the normal.<br />
The ratio of the sine of the angle between the normal<br />
and the incident ray, to the sine of the angle<br />
between the normal and the refracted ray, is a constant<br />
for a given wavelength of incident light.<br />
Also see refraction.<br />
source. In fiberoptic sensors, as in communications,<br />
that part of a syatem from which signals or messages<br />
are considered to originate. A fiberoptic sensor is<br />
the source of baseband signals in a fiberoptic system.<br />
The source may be an optical source (unmodulated)<br />
or a signal source used to modulate the optical<br />
source. See light source.<br />
source-free medium. In fiberoptic, a transmission<br />
medium that does not contain a source of electromagnetic<br />
radiation, such as electric charges or magnetic<br />
poles, other than a propagating or standing<br />
electromagnetic wave.<br />
space-division multiplexing. The use of spatial separation<br />
between light beams, conductors, optical<br />
fibers or other transmission media in order to obtain<br />
channel isolation. For example, the combining<br />
of several independent and isolated fibers or wires<br />
in a single bundle or cable in order to use each<br />
fiber (or bundle) as a separate communication path,<br />
channel, or set of channels. A typical arrangement<br />
for multiplexing might be to use time-division multiplexing<br />
on each space-division multiplexed fiber pair<br />
in an optical cable.<br />
splitter.<br />
See beam splitter.<br />
~. In a laser, emission that does<br />
not bear an amplitude, phase, or time relationship<br />
with an applied signal and is therefore a random<br />
noiselike form of light radiation. Alao see stimulated<br />
emission.<br />
spreading.<br />
star-coupler.<br />
See geometric spreading.<br />
See reflective star-coupler.<br />
step-index fiber. A fiber in which there is an abrupt<br />
change in refractive index between the core and<br />
cladding along a fiber diameter, with the core refractive<br />
index being higher than the cladding refractive<br />
index. There may be more then one layer,<br />
each layer with a different refractive index that<br />
is uniform throughout the layer, but usually with<br />
decreasing indices in the outside layers.<br />
stimulated emission. In a laser, the emission of light<br />
caused by a signal applied to the laser such that<br />
the response is directly proportional to, and in<br />
phase coherence with, the electromagnetic field of<br />
the stimulating signal. This coherency between applied<br />
signal and response contributes to the usefulness<br />
of the laaer. Also see spontaneous emission.<br />
stimulated emission of radiation. See light amplification<br />
by stimulated emission of radiation (laser).<br />
strength member. In fiberoptic cables, a component of<br />
the cable that provides tensile strength and bending<br />
resistance, therefore limiting stress (and strain)<br />
on the optical fibers in the cable.<br />
stripper.<br />
See cladding mode stripper.<br />
substrate. A material used to support or serve as a<br />
foundation, vehicle, or carrier for other material<br />
that has the required characteristics for specific<br />
application but does not have the proper phyaical<br />
strength to support itself, e.g., a block of material<br />
upon which active materials may be deposited by<br />
evaporative techniques or on which active materials<br />
may be bonded by cementing or etching techniques.<br />
The substrate is usually inert or passive relative<br />
to the active material mounted upon it.<br />
switch.<br />
See waveguide switch.<br />
solid state. Pertaining to the conduction of electric<br />
currents or magnetic flux, or the propagation of<br />
electromagnetic waves, within materials other than<br />
gases or other than a vacuum.<br />
A-20
— TDM.<br />
T<br />
See time-division multiplexing.<br />
telecommunication. Communication over relatively large<br />
distances by any transmission, emission, or recep -<br />
tion of signals, signa, writing, images, and sounds,<br />
or intelligence of any nature by wire, radio, visual,<br />
or other electrical, electromagnetic, optical,<br />
acoustic, or mechanical means. The process enables<br />
one or more users to pass to one or more other users<br />
information of any nature delivered in desirable<br />
forms, such as written or printed matter, fixed or<br />
moving pictures, words, music, visible or audible<br />
signals, or signals that can control the functioning<br />
of equipment or mechanisms. Also see telemetry.<br />
telemetry. The branch of science and technology devoted<br />
to the process of measuring the values of variables,<br />
such as pressure, temperature, humidity, blood flow,<br />
radiation levels, or sound levels; transmitting the<br />
results of the measurements by some means to a distant<br />
station; and interpreting, indicating, displaying,<br />
recording, or using the information that is<br />
obtained. Also see telecommunication.<br />
time.<br />
See coherence time.<br />
time-division multiplexing (TDM). Multiplexing in which<br />
separate channels are established by connecting one<br />
circuit automatically to many signal sources sequentially<br />
in time. The signals from the several<br />
sources, such as an array of fiberoptic sensors,<br />
share the time of the circuit by using the circuit<br />
in successive time slots. Each discrete time interval<br />
is assigned to a particular signal source. Synchronizing<br />
pulses are used to asaist in demultiplexing<br />
at the distant end of the circuit. Thus, the<br />
time of an optical fiber can be divided among many<br />
signal sources, by allowing two or more signal<br />
sources to use the channel at different times. The<br />
channel may be shared by automatically switching to<br />
the several sources and connecting each one to the<br />
channel during the specific time period allocated<br />
to that source. For example, if each aource is assigned<br />
to a given channel for 1 Vsec out of each<br />
millisecond, 1,000 sources can be accommodated<br />
(multiplexed) by the channel. During a given time<br />
interval the entire available frequency spectrum<br />
can be used by the channel to which it is assigned.<br />
In general, time-division multiplexed systema use<br />
pulae transmission or analog sampling. The multiplexed<br />
pulse string may be considered to be the<br />
interleaved pulse strings of the individual channels.<br />
The individual channel pulses may be modulated in<br />
either an analog or digital manner.<br />
total internal reflection. Reflection that occurs within<br />
a substance when the incidence angle of a light<br />
ray striking a boundary surface is greater than the<br />
critical angle and therefore the entire energy of<br />
the ray is reflected back into the substance and<br />
none is transmitted across the surface.<br />
total internal reflection senaor. See near total internal<br />
reflection sensor.<br />
transducer. A device capable of transforming energy<br />
from one form to another, usually with such fidelity<br />
that if the original energy time and spatial distribution<br />
represents information, the transformed energy<br />
can represent the same information or a function<br />
A-21<br />
of that information. For example, a fiberoptic sensor<br />
that converts a pulse pressure wave into a modulated<br />
lightwave, a microphone that converts a sound<br />
wave to a corresponding electrical current, a modulated<br />
laser that converta electrical currents to<br />
modulated lightwaves, a photodetector that converts<br />
modulated lightwaves to electrical current, or a<br />
piezoelectric crystal that produces a voltage proportional<br />
to the time derivative of the pressure<br />
wave that impinges upon it. See optoacoustic transducer.<br />
transmission coefficient. The ratio of the transmitted<br />
field strength to the incident field strength when<br />
an electromagnetic wave is incident upon an interface<br />
surface between dielectric media of different<br />
refractive indices. If, at oblique incidence, the<br />
electric field component of the incident wave is<br />
parallel to the interface, the transmission coefficient<br />
is given by:<br />
T = 2n2cosA/(n2cosA + nlcosB)<br />
where nl and n2 are the reciprocals of the refractive<br />
indices of the incident and transmitted media,<br />
respectively, and A and B are the incidence angle<br />
and refraction angle (with respect to the normal to<br />
the interface surface), respectively. If, at oblique<br />
incidence, the magnetic field component of the<br />
incident wave is parallel to the interface surface,<br />
the transmission coefficient is given by:<br />
T = 2n2cosA/(nlcosA + n2cosB)<br />
These equations are known as the Fresnel equations<br />
for these cases.<br />
transmission medium. Any subatance that can be or Is<br />
used for the propagation of signals, usually in the<br />
form of modulated radio, light, acoustic waves, or<br />
electric currents, from one point to another, such<br />
as an optical fiber, cable, or bundle; a wire; a<br />
dielectric slab; water; or air. Free space can also<br />
be considered as a transmission medium for electromagnetic<br />
waves.<br />
transmitted power. The energy per unit time usually<br />
expressed in watta, propagated through a specified<br />
croas sectional area, such as a fiber cable or other<br />
waveguide, or a specified cross-sectional area perpendicular<br />
to the direction of propagation, such as<br />
in a specified solid angle, or through a fictitious<br />
sphere completely surrounding the transmitter. Since<br />
instantaneous transmitted power can vary with time<br />
and the specified croas-sectional area can change,<br />
the power can assume various forms of measurement,<br />
such as the peak envelope power, the power in a given<br />
direction, the power averaged over time, the power<br />
averaged over an area or solid angle, the total carrier<br />
power delivered to an antenna, the total power<br />
radiated and integrated over all directions, or it<br />
may be the power limited to a specified portion of<br />
a frequency spectrum or bandwidth.<br />
trapping.<br />
See ray trapping.
v<br />
vacancy defect. In the somewhat ordered array of atoms<br />
and molecules in optical-fiber material, a site at<br />
which an atom or molecule is missing in the array.<br />
The defect can serve as a scattering center, causing<br />
diffusion, heating, absorption and resultant attenuation.<br />
Also see interstitial defect.<br />
valence band. In a semiconductor, the range of electron<br />
energy, lower than that of the conduction<br />
band, possessed by electrons that are held bound to<br />
an atom of the material, thus reducing conductivity<br />
for electric currents even under the influence of<br />
an applied electric field. When electron engergies<br />
are raised, e.g., by thermal excitation or by phonons,<br />
electrons with the highest energy levels of<br />
the valence band are raised to the lower energy<br />
levels of the conduction band, thus leaving holes<br />
in the atoms whose electrons remain in the valence<br />
band.<br />
velocity.<br />
See phase velocity.<br />
V-parameter. A parameter that can be used to calculate<br />
or express the number of propagating modes that a<br />
step-indexed optical fiber is capable of supporting,<br />
expressed mathematically as:<br />
fn =<br />
(2na/k)(n12 - n22)1/2<br />
where fn is the V-parameter (V-value or normalized<br />
frequency), a is the optical fiber core radius, Ais<br />
the source wavelength, and nl and n2 are the refractive<br />
indices of the core and cladding of the optical<br />
fiber. For a large number of modes, the mode volume<br />
is given by:<br />
N = fn2/2<br />
where N is the number of modes, or mode volume, and<br />
fn Is the V-parameter (V-value or normalized frequency)<br />
above. Synonymous with normalized frequency;<br />
V-value.<br />
V-value. Synonym for V-parameter.<br />
wave.<br />
w<br />
See electromagnetic wave; evanescent wave.<br />
wave equation. The equation, based on Maxwell’s equations,<br />
the constitutive relations, and the vector<br />
algebra, that relates the electromagnetic field of<br />
an electromagnetic wave time and space derivatives<br />
with the transmission medium electrical permittivity<br />
and magnetic permeability in a region without electrical<br />
charges or currents. The solution of the wave<br />
equation yields the electric and magnetic field<br />
strength everywhere as a function of time and space<br />
coordinates, field strengths, and transmission media<br />
parameters. The wave equation is given as either:<br />
72H- ~ca2H/at2 = o ‘r<br />
v2E - vEa2E/at2 = o<br />
in a current- and charge-free nonconducting medium,<br />
where E is the electric field intensity, H is the<br />
magnetic field intensity, c is the electric permittivity,<br />
and p is the magnetic permeability. V is the<br />
vector spatial derivative operator. The wave equation<br />
applies in optical waveguides.<br />
wavefront. A surface normal to an electromagnetic ray<br />
as it propagates from a source, the surface of the<br />
wavefront passing through those parts of the waves<br />
that are in the same phase. For parallel rays, the<br />
wavefront is a plane. For rays diverging from or<br />
converging toward a point, the wavefront is spherical.<br />
The wavefront is perpendicular to the direction<br />
of propagation of the wave, and the electric<br />
and magnetic field vectors of the wave define a<br />
plane that is tangent to the wavefront surface at<br />
the point that the field vectors are determined.<br />
The front is a three-dimensional surface all the<br />
points on which are the same optical path length<br />
from the wave source.<br />
waveguide. Any structure capable of confining and supporting<br />
the energy of an electromagnetic wave to a<br />
specific relatively narrow controllable path that is<br />
capable of being altered, such as a rectangular<br />
cross-section metal pipe, an optical fiber of circular<br />
cross section, or a coaxial cable. See slab<br />
dielectric waveguide.<br />
waveguide delay distortion. In an optical waveguide,<br />
the distortion in received signal caused by the differences<br />
in propagation time for each wavelength,<br />
(i.e., the delay versus wavelength effect for each<br />
propagating mode), causing a spreading of a received<br />
signal pulse at the detector. Waveguide delay distortion<br />
contributes to group-delay distortion as<br />
does material dispersion and multimode group-delay<br />
spread.<br />
waveguide dispersion. The part of the total dispersion<br />
attributable to the dimensions of the waveguide. The<br />
cross-section dimensions are critical. They determine<br />
the modes that are allowed and not allowed to<br />
propagate. Waveguide dispersion increases as the<br />
spectral width of the source increases due to the<br />
actual dimensions and their variation along the<br />
length of the guide.<br />
wavelength. The length of a wave measured from any<br />
point on a wave to the corresponding point on the<br />
next cycle of the wave, such as from crest to crest.<br />
Wavelength determines the nature of the various<br />
forms of radiant energy that comprise the electromagnetic<br />
spectrum, e.g., it determines the color of<br />
light. For a sinusoidal wave, the wavelength is the<br />
distance between points of corresponding phase of<br />
two consecutive cycles of the wave. The wavelength<br />
k, iS related to the phase velocity v, and the frequency<br />
f, by the relation i= vlf.<br />
wavelength-division multiplexingg (WDM). In optical communication<br />
systems, the multiplexing of lightwaves in<br />
a single transmission medium or channel, such that<br />
each of the waves are of a different wavelength and<br />
are modulated separately before insertion into the<br />
medium. Usually, several sources are used, such as<br />
a laser, or several lasera, or a dispersed white<br />
light source or aources, each having a distinctly<br />
different center wavelength. WDM is the same as<br />
frequency-division multiplexing (FDM) applied to<br />
visible light frequencies of the electromagnetic<br />
spectrum.<br />
wave number. The value of 2n times the reciprocal of<br />
the wavelength of a single-frequency sinusoidal wave<br />
such as a singlefrequency uniform plane-polarized<br />
A-22
electromagnetic wave, e.g. , a monochromatic lightwave.<br />
The wave number is usually used for waves in<br />
or near the visible spectrum, since wavelength is<br />
more readily measured than frequency, but it is frequency,<br />
or wave number, that iS directly related to<br />
to energy. For example, photon energy is given by:<br />
P.E.<br />
= hkc/2n = hf = hcl~<br />
where h is Planck’s constant, k is the wave number,<br />
c is the velocity of the light, f 1S the frequency,<br />
and k is the wavelength. The wave number is the<br />
number of wavelengths per unit distance in the direction<br />
of propagation. Also see wave parameter.<br />
waveguide switch. A mechanically or electrically controlled<br />
device that is capable of stopping, attenuating,<br />
or diverting the propagation of electromagnetic<br />
energy at a specific point in a waveguide.<br />
wave parameter. 1. Any feature of a wave, such as its<br />
amplitude, phase or shape. 2. A unit that is used<br />
in regard to periodic waves, such as electromagnetic<br />
waves. The wave parameter, p, is given by the relation<br />
p = 2n/A, where A is the wavelength. Also see<br />
wave number.<br />
— WDM.<br />
See wavelength-division multiplexing.<br />
3-dB coupler. In fiberoptic, a coupler that splits<br />
the optical energy in an optical waveguide into two<br />
equal parts and couples each part into a separate<br />
waveguide. The 3-dB coupler ideally distributea 50%<br />
of the input optical power to each of the output<br />
channels. However, in actual practice, the ratio<br />
may vary, for example, 45% into one and 55% into the<br />
other output channel. Some optical energy may be<br />
lost or absorbed by the coupler.<br />
A-23