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4.6 EVALUATION OF GROUND SETTLEMENTS FOLLOWING<br />
CYCLIC LOADING<br />
As excess pore pressure generated by cyclic loading dissipates due to drainage, the soil consolidates,<br />
which results in ground settlement. Similarly, non-saturated cohesionless soils will contract during<br />
cyclic shearing resulting in surface settlements. The magnitude of the settlements will reflect the<br />
density of the soil, intensity of the ground motions, the factor of safety against liquefaction, and the<br />
thickness of the loose soil deposit. Field observations document post-earthquake settlements of soils<br />
adjacent to bridges of over 1 m (Hamada et al. 1995; Yasuda et al. 1996). These include flat sites in<br />
the absence of lateral spreading. Damage modes include pavement damage, uneven grades at the<br />
transition from soil to pile-supported approach structures, and abutment damage (Seed et al. 1990;<br />
Yasuda et al. 1996).<br />
Several methods have been developed for estimating the magnitude of earthquake-induced<br />
settlements in sandy soils. The most widely adopted methods have been developed by Ishihara<br />
and Yoshimine (1992) and Tokimatsu and Seed (1987). The method proposed by Ishihara and<br />
Yoshimine has been produced in the form of a design chart relating volumetric strain in sandy<br />
soils to soil density and the factor of safety against liquefaction (FS L ; Figure 4.12). This analysis<br />
requires that FS L be computed for the sandy deposit, or each sub-layer within the deposit. The<br />
methods outlined in Chapter 3 for estimating the triggering of liquefaction are used. The percent<br />
compression of each sub-layer can then be easily estimated by using Figure 4.12.<br />
Although the procedure of Ishihara and Yoshimine was developed for saturated sandy soils it can be<br />
applied for unsaturated soils in an approximate manner. This assumes that volumetric behavior of a<br />
dry or partially saturated sand during drained cyclic loading is similar to the volumetric behavior of<br />
the soil following the application of undrained cyclic loading on a saturated specimen (i.e., postloading<br />
consolidation due to the dissipation of excess pore pressure). In both scenarios the<br />
volumetric strain that is developed is a function of the initial void ratio of the soil, the effective<br />
confining stress prior to cyclic loading, and the intensity and duration of the cyclic loading.<br />
As illustrated in Figure 4.12, in order to estimate the volumetric strain the factor of safety against<br />
liquefaction must be obtained. This calculation accounts for the influence of the four factors (e, ′ c ,<br />
CSR, MSF) previously listed on the estimated volumetric strain. Clearly, an unsaturated soil is not<br />
prone to liquefaction regardless of its density; therefore the concept of developing a factor of safety<br />
against liquefaction does not seem appropriate for this scenario. However, loose to medium dense<br />
sandy soils will experience volumetric strains during loading. A possible approach for applying the<br />
method to unsaturated soils is to first compute the FS L as if the soil were saturated, then enter the<br />
chart at the appropriate FS L and density. The results of this approximation should be tempered by<br />
calculations using the Tokimatsu and Seed method as follows. Because the Ishihara procedure was<br />
developed for clean sands, a correction is required for silty sands and silts. The (N 1 ) 60 values should<br />
be modified using correction factors for fines content (Youd and Idriss 1997) prior to using Figure<br />
4.12. Also, the N 1 -values shown in Figure 4.12 correspond to typical Japanese equipment and<br />
procedures, and are thus representative of an SPT energy ratio of approximately ER m = 55%. The<br />
corrected and standardized SPT (N 1 ) 60 values used to develop estimates of FS L should be increased<br />
by about 10% when using Figure 4.12 to estimate the resulting volumetric compression.<br />
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