Experimental and Numerical Analysis of a PCM-Supported ...
Experimental and Numerical Analysis of a PCM-Supported ...
Experimental and Numerical Analysis of a PCM-Supported ...
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Several models <strong>and</strong> approaches for mass transfer coefficients on both the gas <strong>and</strong><br />
liquid sides are presented by Wagner et al. [40]. Various approaches <strong>and</strong> models for<br />
determination <strong>of</strong> the wetted <strong>and</strong> effective interfacial areas for mass transfer<br />
presented by Kister [32] <strong>and</strong> G<strong>and</strong>hidasan [41] were preliminary examined <strong>and</strong><br />
compared against each other.<br />
One particular problem to address here is the significant discrepancies between the<br />
predicted values <strong>of</strong> mass transfer coefficients between various approaches <strong>and</strong><br />
models. It is observed that many researchers have used Onda et al. [35] model to<br />
describe the liquid-gas interfacial areas <strong>and</strong> mass transfer coefficient in distillation<br />
columns. Klausner et al. [45] have already developed a detailed heat <strong>and</strong> mass<br />
transfer analysis for a HDH system called the diffusion driven desalination (DDD)<br />
process. They extensively tested Onda et al. [35] correlations <strong>and</strong> used it to evaluate<br />
the mass transfer coefficients on the liquid <strong>and</strong> gas sides. They reported that<br />
excellent results were obtained against experimentation measurements [47]; thus<br />
the same approach will be applied here.<br />
Nevertheless, Klausner <strong>and</strong> Mei [45-46] modified Onda et al. [35] model described<br />
by equations (4.46-4.47) by introducing a constant <strong>of</strong> 2.2 instead <strong>of</strong> 1.45 for<br />
calculating the wetted interfacial area in the (DDD) system. They argued that the<br />
model underestimates the wetted surface area <strong>of</strong> the packing <strong>and</strong> this was the<br />
reason behind this modification in equation (4.47). The model is based on the<br />
concept <strong>of</strong> wetted packing area as a geometric parameter in determining the<br />
Reynolds number for the liquid as opposed to the interfacial area.<br />
a<br />
a<br />
e<br />
<br />
<br />
<br />
c<br />
exp 1.45<br />
<br />
<br />
<br />
<br />
l <br />
0.75<br />
0.1 0.2 0.<br />
05<br />
1 Rel<br />
Wel<br />
Frl<br />
<br />
<br />
<br />
<br />
(4.46)<br />
a<br />
w<br />
a<br />
<br />
<br />
<br />
<br />
<br />
<br />
c<br />
exp <br />
2.2<br />
<br />
<br />
<br />
<br />
L <br />
0.75<br />
0.5 0.2 0.<br />
05<br />
1 Re<br />
LA<br />
WeL<br />
Fr<br />
L<br />
<br />
<br />
<br />
<br />
<br />
<br />
(4.47)<br />
Therefore, this modification could be even more crucial for the present analysis due<br />
to the existence <strong>of</strong> conductive packing media or a solid phase in the energy <strong>and</strong><br />
mass balances. However, their predicted performance using this modified correlation<br />
is always higher than their experimental measurements in terms <strong>of</strong> the outlet air<br />
humidity content, outlet water temperature, <strong>and</strong> outlet air temperature.<br />
In the original model, Onda et al. [35] assumed the wetted area was equal to the<br />
effective interfacial area. The total wetted surface area in the irrigated column is<br />
expected to be greater than the effective area for mass transfer due to existence <strong>of</strong><br />
static liquid holdup which contributes little to heat <strong>and</strong> mass transfer. This finding has<br />
been ascertained during the course <strong>of</strong> preliminary calculations <strong>of</strong> the effective<br />
83