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Thermo, Volume 4, Issue 2 (June 2024) – 6 articles

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22 pages, 1538 KiB  
Article
On the Second Law of Thermodynamics in Continuum Physics
by Claudio Giorgi and Angelo Morro
Thermo 2024, 4(2), 273-294; https://doi.org/10.3390/thermo4020015 - 11 Jun 2024
Cited by 1 | Viewed by 737
Abstract
The paper revisits the formulation of the second law in continuum physics and investigates new methods of exploitation. Both the entropy flux and the entropy production are taken to be expressed by constitutive equations. In three-dimensional settings, vectors and tensors are in order [...] Read more.
The paper revisits the formulation of the second law in continuum physics and investigates new methods of exploitation. Both the entropy flux and the entropy production are taken to be expressed by constitutive equations. In three-dimensional settings, vectors and tensors are in order and they occur through inner products in the inequality representing the second law; a representation formula, which is quite uncommon in the literature, produces the general solution whenever the sought equations are considered in rate-type forms. Next, the occurrence of the entropy production as a constitutive function is shown to produce a wider set of physically admissible models. Furthermore the constitutive property of the entropy production results in an additional, essential term in the evolution equation of rate-type materials, as is the case for Duhem-like hysteretic models. This feature of thermodynamically consistent hysteretic materials is exemplified for elastic–plastic materials. The representation formula is shown to allow more general non-local properties while the constitutive entropy production proves essential for the modeling of hysteresis. Full article
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Figure 1

Figure 1
<p>Plastic model with asymptotic bounds <math display="inline"><semantics> <mrow> <mi>σ</mi> <mo>=</mo> <mo>±</mo> <msub> <mi>σ</mi> <mi>u</mi> </msub> </mrow> </semantics></math> (dashed): hysteresis loops (solid) with <math display="inline"><semantics> <mrow> <mo>Λ</mo> <mo>=</mo> <mn>1</mn> <mo>,</mo> <mn>2</mn> <mo>,</mo> <mn>3</mn> </mrow> </semantics></math> and starting values <math display="inline"><semantics> <mrow> <mrow> <mo>(</mo> <msub> <mi>λ</mi> <mn>0</mn> </msub> <mo>,</mo> <msub> <mi>σ</mi> <mn>0</mn> </msub> <mo>)</mo> </mrow> <mo>=</mo> <mrow> <mo>(</mo> <mn>0</mn> <mo>,</mo> <mn>0</mn> <mo>)</mo> </mrow> <mo>,</mo> <mrow> <mo>(</mo> <mn>0</mn> <mo>,</mo> <mo>−</mo> <mn>0.1</mn> <mo>)</mo> </mrow> </mrow> </semantics></math>.</p>
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<p>Plastic model with nonlinear elastic function: hysteresis loops (solid) with <math display="inline"><semantics> <mrow> <mo>Λ</mo> <mo>=</mo> <mn>2</mn> <mo>,</mo> <mn>5</mn> </mrow> </semantics></math> and starting values <math display="inline"><semantics> <mrow> <mrow> <mo>(</mo> <msub> <mi>λ</mi> <mn>0</mn> </msub> <mo>,</mo> <msub> <mi>σ</mi> <mn>0</mn> </msub> <mo>)</mo> </mrow> <mo>=</mo> <mrow> <mo>(</mo> <mn>0</mn> <mo>,</mo> <mn>0</mn> <mo>)</mo> </mrow> <mo>,</mo> <mrow> <mo>(</mo> <mn>0</mn> <mo>,</mo> <mo>−</mo> <mn>0.1</mn> <mo>)</mo> </mrow> </mrow> </semantics></math>; asymptotic bounds <math display="inline"><semantics> <mrow> <mi>σ</mi> <mo>=</mo> <mo>±</mo> <mo>(</mo> <mn>1</mn> <mo>+</mo> <mi>β</mi> <mo>)</mo> </mrow> </semantics></math> (dashed).</p>
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<p>Elastic–plastic model with asymptotic bounds <math display="inline"><semantics> <mrow> <mi>σ</mi> <mo>=</mo> <mo>±</mo> <msub> <mi>σ</mi> <mi>u</mi> </msub> </mrow> </semantics></math> (dashed) and yielding thresholds <math display="inline"><semantics> <mrow> <mi>σ</mi> <mo>=</mo> <mo>±</mo> <msub> <mi>σ</mi> <mi>y</mi> </msub> </mrow> </semantics></math> (short dashed); hysteresis loops (solid) with amplitude <math display="inline"><semantics> <mrow> <mo>Λ</mo> <mo>=</mo> <mn>4</mn> </mrow> </semantics></math> and starting value <math display="inline"><semantics> <mrow> <mrow> <mo>(</mo> <msub> <mi>λ</mi> <mn>0</mn> </msub> <mo>,</mo> <msub> <mi>σ</mi> <mn>0</mn> </msub> <mo>)</mo> </mrow> <mo>=</mo> <mrow> <mo>(</mo> <mn>0</mn> <mo>,</mo> <mn>0</mn> <mo>)</mo> </mrow> </mrow> </semantics></math>.</p>
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21 pages, 2349 KiB  
Article
An Optimized Artificial Neural Network Model of a Limaçon-to-Circular Gas Expander with an Inlet Valve
by Md Shazzad Hossain, Ibrahim Sultan, Truong Phung and Apurv Kumar
Thermo 2024, 4(2), 252-272; https://doi.org/10.3390/thermo4020014 - 11 Jun 2024
Cited by 1 | Viewed by 657
Abstract
In this work, an artificial neural network (ANN)-based model is proposed to describe the input–output relationships in a Limaçon-To-Circular (L2C) gas expander with an inlet valve. The L2C gas expander is a type of energy converter that has great potential to be used [...] Read more.
In this work, an artificial neural network (ANN)-based model is proposed to describe the input–output relationships in a Limaçon-To-Circular (L2C) gas expander with an inlet valve. The L2C gas expander is a type of energy converter that has great potential to be used in organic Rankine cycle (ORC)-based small-scale power plants. The proposed model predicts the different performance indices of a limaçon gas expander for different input pressures, rotor velocities, and valve cutoff angles. A network model is constructed and optimized for different model parameters to achieve the best prediction performance compared to the classic mathematical model of the system. An overall normalized mean square error of 0.0014, coefficient of determination (R2) of 0.98, and mean average error of 0.0114 are reported. This implies that the surrogate model can effectively mimic the actual model with high precision. The model performance is also compared to a linear interpolation (LI) method. It is found that the proposed ANN model predictions are about 96.53% accurate for a given error threshold, compared to about 91.46% accuracy of the LI method. Thus the proposed model can effectively predict different output parameters of a limaçon gas expander such as energy, filling factor, isentropic efficiency, and mass flow for different operating conditions. Of note, the model is only trained by a set of input and target values; thus, the performance of the model is not affected by the internal complex mathematical models of the overall valved-expander system. This neural network-based approach is highly suitable for optimization, as the alternative iterative analysis of the complex analytical model is time-consuming and requires higher computational resources. A similar modeling approach with some modifications could also be utilized to design controllers for these types of systems that are difficult to model mathematically. Full article
(This article belongs to the Special Issue Innovative Technologies to Optimize Building Energy Performance)
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<p>ORC schematic.</p>
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<p>Valved-expander system.</p>
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<p>Valve operating angle in a half-cycle.</p>
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<p>(<b>a</b>) Outline of inlet DDRV, and (<b>b</b>) Dynamic passage area.</p>
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<p>(<b>a</b>) Computational times and (<b>b</b>) number of REFPROP accesses for the classic mathematical model under different precision values.</p>
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<p>ANN architecture.</p>
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<p>The dataset used for training and testing.</p>
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<p>Flowchart of the training and prediction process.</p>
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<p>Effects of learning rate on (<b>a</b>) <math display="inline"><semantics> <mrow> <mi>M</mi> <mi>S</mi> <mi>E</mi> </mrow> </semantics></math>, (<b>b</b>) <math display="inline"><semantics> <mrow> <mi>M</mi> <mi>A</mi> <mi>E</mi> </mrow> </semantics></math>, and (<b>c</b>) <math display="inline"><semantics> <msup> <mi>R</mi> <mn>2</mn> </msup> </semantics></math>.</p>
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<p>Effects of training function on (<b>a</b>) <math display="inline"><semantics> <mrow> <mi>M</mi> <mi>S</mi> <mi>E</mi> </mrow> </semantics></math>, (<b>b</b>) <math display="inline"><semantics> <mrow> <mi>M</mi> <mi>A</mi> <mi>E</mi> </mrow> </semantics></math>, and (<b>c</b>) <math display="inline"><semantics> <msup> <mi>R</mi> <mn>2</mn> </msup> </semantics></math>.</p>
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<p>Cross-validation score for different training functions: (<b>a</b>) <math display="inline"><semantics> <mrow> <mi>M</mi> <mi>S</mi> <mi>E</mi> </mrow> </semantics></math>, (<b>b</b>) <math display="inline"><semantics> <mrow> <mi>M</mi> <mi>A</mi> <mi>E</mi> </mrow> </semantics></math>, and (<b>c</b>) <math display="inline"><semantics> <msup> <mi>R</mi> <mn>2</mn> </msup> </semantics></math>.</p>
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<p>Effects of hidden layer size on (<b>a</b>) <math display="inline"><semantics> <mrow> <mi>M</mi> <mi>S</mi> <mi>E</mi> </mrow> </semantics></math>, (<b>b</b>) <math display="inline"><semantics> <mrow> <mi>M</mi> <mi>A</mi> <mi>E</mi> </mrow> </semantics></math>, and (<b>c</b>) <math display="inline"><semantics> <msup> <mi>R</mi> <mn>2</mn> </msup> </semantics></math>.</p>
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<p>Effects of activation function on (<b>a</b>) <math display="inline"><semantics> <mrow> <mi>M</mi> <mi>S</mi> <mi>E</mi> </mrow> </semantics></math>, (<b>b</b>) <math display="inline"><semantics> <mrow> <mi>M</mi> <mi>A</mi> <mi>E</mi> </mrow> </semantics></math>, and (<b>c</b>) <math display="inline"><semantics> <msup> <mi>R</mi> <mn>2</mn> </msup> </semantics></math>.</p>
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<p>Effects of epoch size on (<b>a</b>) <math display="inline"><semantics> <mrow> <mi>M</mi> <mi>S</mi> <mi>E</mi> </mrow> </semantics></math>, (<b>b</b>) <math display="inline"><semantics> <mrow> <mi>M</mi> <mi>A</mi> <mi>E</mi> </mrow> </semantics></math>, and (<b>c</b>) <math display="inline"><semantics> <msup> <mi>R</mi> <mn>2</mn> </msup> </semantics></math>.</p>
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<p>Energy (<b>a</b>) prediction, (<b>b</b>) error histogram, and (<b>c</b>) error distribution.</p>
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<p>Filling factor (<b>a</b>) prediction, (<b>b</b>) error histogram, and (<b>c</b>) error distribution.</p>
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<p>Isentropic efficiency (<b>a</b>) prediction, (<b>b</b>) error histogram, and (<b>c</b>) error distribution.</p>
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<p>Mass flow (<b>a</b>) prediction, (<b>b</b>) error histogram, and (<b>c</b>) error distribution.</p>
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<p>Overall normalized prediction error histogram.</p>
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30 pages, 9528 KiB  
Article
Comparative Numerical Analysis of Keyhole Shape and Penetration Depth in Laser Spot Welding of Aluminum with Power Wave Modulation
by Saeid SaediArdahaei and Xuan-Tan Pham
Thermo 2024, 4(2), 222-251; https://doi.org/10.3390/thermo4020013 - 23 May 2024
Cited by 1 | Viewed by 853
Abstract
Keyhole mode laser welding is a valuable technique for welding thick materials in industrial applications. However, its susceptibility to fluctuations and instabilities poses challenges, leading to defects that compromise weld quality. Observing the keyhole during laser welding is challenging due to bright process [...] Read more.
Keyhole mode laser welding is a valuable technique for welding thick materials in industrial applications. However, its susceptibility to fluctuations and instabilities poses challenges, leading to defects that compromise weld quality. Observing the keyhole during laser welding is challenging due to bright process radiation, and existing observation methods are complex and expensive. This paper alternatively presents a novel numerical modeling approach for laser spot welding of aluminum through a modified mixture theory, a modified level-set (LS) method, and a thermal enthalpy porosity technique. The effects of laser parameters on keyhole penetration depth are investigated, with a focus on laser power, spot radius, frequency, and pulse wave modulation in pulsed wave (PW) versus continuous wave (CW) laser welding. PW laser welding involves the careful modulation of power waves, specifically adjusting the pulse width, pulse number, and pulse shapes. Results indicate a greater than 80 percent increase in the keyhole penetration depth with higher laser power, pulse width, and pulse number, as well as decreased spot radius. Keyhole instabilities are also more pronounced with higher pulse width/numbers and frequencies. Notably, the rectangular pulse shape demonstrates substantially deeper penetration compared to CW welding and other pulse shapes. This study enhances understanding of weld pool dynamics and provides insights into optimizing laser welding parameters to mitigate defects and improve weld quality. Full article
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Figure 1
<p>Schematic depiction of (<b>a</b>) 2D axisymmetric configuration of laser welding with Gaussian distribution used in the simulation and (<b>b</b>,<b>c</b>) 3D illustration of the problem generated in COMSOL Multiphysics 5.6 with definitions of the transversal cross-section of the domain and the plane used to monitor the keyhole morphology and penetration.</p>
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<p>Complete schematic of all the laser energy pulse shapes used for power modulation for (<b>a</b>) MW10-MW14 and (<b>b</b>) MW15-MW17.</p>
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<p>Computational domain and the generated extra fine mapped mesh.</p>
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<p>Comparison of (<b>a</b>) the keyhole morphology between the simulation (orange) and experimental (blue) results of Qin et al. [<a href="#B33-thermo-04-00013" class="html-bibr">33</a>] and (<b>b</b>) the keyhole diameter on the surface.</p>
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<p>Schematic depiction of the keyhole, molten pool, driving forces and pressures, mushy zone, solidus, and liquidus temperature lines.</p>
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<p>Keyhole penetration procedure for case LC10 with 6 kW laser power, 3 ms pulse width, and 300 µm spot radius.</p>
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<p>Keyhole penetration procedure for case LC10 with 6 kW laser power, 3 ms pulse width, and 300 µm spot radius.</p>
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<p>Morphology of keyhole for different spot radii after 2 ms of laser welding for (<b>a</b>) 300 µm spot radius, (<b>b</b>) 425 µm spot radius, (<b>c</b>) 525 µm spot radius, and (<b>d</b>) 725 µm spot radius.</p>
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<p>Morphology of keyhole for different laser frequencies after three pulses for (<b>a</b>) 50 Hz, (<b>b</b>) 100 Hz, and (<b>c</b>) 150 Hz.</p>
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<p>Morphology of keyhole for different laser frequencies at the end of the first and second pulse periods for (<b>a</b>) 50 Hz, (<b>b</b>) 100 Hz, and (<b>c</b>) 150 Hz.</p>
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<p>Morphology of keyhole for different laser frequencies at the end of the first and second pulse periods for (<b>a</b>) 50 Hz, (<b>b</b>) 100 Hz, and (<b>c</b>) 150 Hz.</p>
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<p>Morphology of keyhole for different laser powers after 3 ms for (<b>a</b>) 2 kW, (<b>b</b>) 4 kW, and (<b>c</b>) 6 kW.</p>
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<p>Morphology of the keyhole for different pulse widths of (<b>a</b>) 0.5 ms, (<b>b</b>) 1 ms, (<b>c</b>) 2 ms, and (<b>d</b>) 3 ms.</p>
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<p>Morphology of the keyhole for different numbers of pulses: (<b>a</b>) 2 pulses, (<b>b</b>) 6 pulses, (<b>c</b>) 10 pulses, (<b>d</b>) 14 pulses, and (<b>e</b>) 18 pulses.</p>
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<p>Morphology of keyhole for different pulse shapes, including (<b>a</b>) continuous welding, (<b>b</b>) rectangular pulse welding, (<b>c</b>) trapezium type 2, (<b>d</b>) trapezium type 1, (<b>e</b>) variant–rectangular, (<b>f</b>) triangular pulse welding, (<b>g</b>) rectangular–trapezium, (<b>h</b>) rectangular–triangular, and (<b>i</b>) rectangular–rectangular (rectangular).</p>
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<p>Maximum temperature variations within Domain 2, considering different (<b>a</b>) laser spot radii, (<b>b</b>) laser frequencies, and (<b>c</b>) laser powers.</p>
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<p>Maximum temperature variations within Domain 2, considering different (<b>a</b>) pulse widths and (<b>b</b>) pulse numbers.</p>
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<p>Maximum temperature variations within Domain 2, considering different pulse shapes, compared to CW for (<b>a</b>) MW10-14 and (<b>b</b>) MW15-1.</p>
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20 pages, 3355 KiB  
Article
The Effect of Temperature on the London Dispersive and Lewis Acid-Base Surface Energies of Polymethyl Methacrylate Adsorbed on Silica by Inverse Gas Chromatography
by Tayssir Hamieh
Thermo 2024, 4(2), 202-221; https://doi.org/10.3390/thermo4020012 - 17 May 2024
Viewed by 705
Abstract
Inverse gas chromatography at infinite dilution was used to determine the surface thermodynamic properties of silica particles and PMMA adsorbed on silica, and more particularly, to quantify the London dispersive energy γsd, the Lewis acid γs+, and [...] Read more.
Inverse gas chromatography at infinite dilution was used to determine the surface thermodynamic properties of silica particles and PMMA adsorbed on silica, and more particularly, to quantify the London dispersive energy γsd, the Lewis acid γs+, and base γs polar surface energies of PMMA/silica composites as a function of the temperature and the recovery fraction θ of PMMA. The polar acid-base surface energy γsAB and the total surface energy of the different composites were then deduced as a function of the temperature. In this paper, the Hamieh thermal model was used to quantify the surface thermodynamic energy of polymethyl methacrylate (PMMA) adsorbed on silica particles at different recovery fractions. A comparison of the new results was carried out with those obtained by applying other molecular models of the surface areas of organic molecules adsorbed on the different solid substrates. An important deviation of these molecular models from the thermal model was proved. The determination of γsd, γs+, γs, and γsAB of PMMA in both the bulk and adsorbed phases showed an important non-linearity variation of these surface parameters as a function of the temperature. The presence of maxima in the curves of γsd(T) highlighted the second-order transition temperatures in PMMA showing beta-relaxation, glass transition, and liquid–liquid temperatures. These three transition temperatures depended on the adsorption rate of PMMA on silica. The proposed method gave a new relation between the recovery fraction of PMMA and its London dispersive energy, showing an important effect of the temperature on the surface energy parameters of the adsorption of PMMA on silica. A universal equation relating γsd(T,θ) of the systems PMMA/silica to the recovery fraction and the temperature was proposed. Full article
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Graphical abstract

Graphical abstract
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<p>Evolution of the London dispersive surface energy <math display="inline"><semantics> <mrow> <msubsup> <mrow> <mi>γ</mi> </mrow> <mrow> <mi>s</mi> </mrow> <mrow> <mi>d</mi> </mrow> </msubsup> <mfenced separators="|"> <mrow> <mi>T</mi> </mrow> </mfenced> </mrow> </semantics></math> (mJ/m<sup>2</sup>) of silica particles as a function of the temperature using the Hamieh thermal model. The dotted line represents the parabolic interpolation of the variations of <math display="inline"><semantics> <mrow> <msubsup> <mrow> <mi>γ</mi> </mrow> <mrow> <mi>s</mi> </mrow> <mrow> <mi>d</mi> </mrow> </msubsup> <mfenced separators="|"> <mrow> <mi>T</mi> </mrow> </mfenced> </mrow> </semantics></math> and the red triangles represent the experimental values.</p>
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<p>Variations of <math display="inline"><semantics> <mrow> <msubsup> <mrow> <mi>γ</mi> </mrow> <mrow> <mi>s</mi> </mrow> <mrow> <mi>d</mi> </mrow> </msubsup> <mo> </mo> <mo stretchy="false">(</mo> <mi>T</mi> <mo stretchy="false">)</mo> </mrow> </semantics></math> of silica particles as a function of the temperature using the various models compared to the Hamieh thermal model. The dotted line represents the parabolic interpolation of the variations of <math display="inline"><semantics> <mrow> <msubsup> <mrow> <mi>γ</mi> </mrow> <mrow> <mi>s</mi> </mrow> <mrow> <mi>d</mi> </mrow> </msubsup> <mfenced separators="|"> <mrow> <mi>T</mi> </mrow> </mfenced> </mrow> </semantics></math> obtained by the Hamieh thermal model.</p>
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<p>Variations of <math display="inline"><semantics> <mrow> <msubsup> <mrow> <mi>γ</mi> </mrow> <mrow> <mi>s</mi> </mrow> <mrow> <mi>d</mi> </mrow> </msubsup> <mo> </mo> <mo stretchy="false">(</mo> <mi>T</mi> <mo stretchy="false">)</mo> </mrow> </semantics></math> of PMMA in bulk phase as a function of the temperature using the various molecular models.</p>
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<p>Variations of <math display="inline"><semantics> <mrow> <msubsup> <mrow> <mi>γ</mi> </mrow> <mrow> <mi>s</mi> </mrow> <mrow> <mi>d</mi> </mrow> </msubsup> <mo> </mo> <mo stretchy="false">(</mo> <mi>T</mi> <mo stretchy="false">)</mo> </mrow> </semantics></math> of PMMA as a function of the temperature using the Hamieh thermal model. The dashed line is relative to the curve without considering the transition phenomenon and the red line shows the three transition temperatures.</p>
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<p>Variations of <math display="inline"><semantics> <mrow> <msubsup> <mrow> <mi>γ</mi> </mrow> <mrow> <mi>s</mi> </mrow> <mrow> <mi>d</mi> </mrow> </msubsup> <mo> </mo> <mo stretchy="false">(</mo> <mi>T</mi> <mo stretchy="false">)</mo> </mrow> </semantics></math> of PMMA adsorbed on silica particles as a function of the temperature at different recovery fractions from <math display="inline"><semantics> <mrow> <mi>θ</mi> <mo>=</mo> <mn>0.31</mn> </mrow> </semantics></math> to <math display="inline"><semantics> <mrow> <mi>θ</mi> <mo>=</mo> <mn>1.0</mn> </mrow> </semantics></math> using the various molecular models: (<b>a</b>) <math display="inline"><semantics> <mrow> <mi>θ</mi> <mo>=</mo> <mn>0.31</mn> </mrow> </semantics></math>, (<b>b</b>) <math display="inline"><semantics> <mrow> <mi>θ</mi> <mo>=</mo> <mn>0.54</mn> </mrow> </semantics></math>, (<b>c</b>) <math display="inline"><semantics> <mrow> <mi>θ</mi> <mo>=</mo> <mn>0.83</mn> </mrow> </semantics></math>, (<b>d</b>) <math display="inline"><semantics> <mrow> <mi>θ</mi> <mo>=</mo> <mn>0.98</mn> </mrow> </semantics></math>, and (<b>e</b>) <math display="inline"><semantics> <mrow> <mi>θ</mi> <mo>=</mo> <mn>1.0</mn> </mrow> </semantics></math>.</p>
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<p>Evolution of the transition temperatures of PMMA adsorbed on silica particles as a function of the recovery fraction PMMA/silica.</p>
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<p>Variations of the London dispersive energy of silica and PMMA adsorbed on silica particles as a function of the temperature and the recovery fraction PMMA/Silica. (<b>a</b>) <math display="inline"><semantics> <mrow> <msubsup> <mrow> <mi>γ</mi> </mrow> <mrow> <mi>s</mi> </mrow> <mrow> <mi>d</mi> </mrow> </msubsup> <mo stretchy="false">(</mo> <mi>T</mi> <mo stretchy="false">)</mo> </mrow> </semantics></math> and (<b>b</b>) <math display="inline"><semantics> <mrow> <msubsup> <mrow> <mi>γ</mi> </mrow> <mrow> <mi>s</mi> </mrow> <mrow> <mi>d</mi> </mrow> </msubsup> <mo stretchy="false">(</mo> <mi>θ</mi> <mo stretchy="false">)</mo> </mrow> </semantics></math>.</p>
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<p>Variations of <math display="inline"><semantics> <mrow> <msubsup> <mrow> <mi>γ</mi> </mrow> <mrow> <mi>s</mi> </mrow> <mrow> <mo>+</mo> </mrow> </msubsup> <mo stretchy="false">(</mo> <mi>T</mi> <mo stretchy="false">)</mo> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <msubsup> <mrow> <mi>γ</mi> </mrow> <mrow> <mi>s</mi> </mrow> <mrow> <mo>−</mo> </mrow> </msubsup> <mo stretchy="false">(</mo> <mi>T</mi> <mo stretchy="false">)</mo> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <msubsup> <mrow> <mi>γ</mi> </mrow> <mrow> <mi>s</mi> </mrow> <mrow> <mi>A</mi> <mi>B</mi> </mrow> </msubsup> <mo stretchy="false">(</mo> <mi>T</mi> <mo stretchy="false">)</mo> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <msubsup> <mrow> <mi>γ</mi> </mrow> <mrow> <mi>s</mi> </mrow> <mrow> <mi>t</mi> <mi>o</mi> <mi>t</mi> <mo>.</mo> </mrow> </msubsup> <mo stretchy="false">(</mo> <mi>T</mi> <mo stretchy="false">)</mo> </mrow> </semantics></math>, and <math display="inline"><semantics> <mrow> <msubsup> <mrow> <mi>γ</mi> </mrow> <mrow> <mi>s</mi> </mrow> <mrow> <mi>d</mi> </mrow> </msubsup> <mo> </mo> <mo stretchy="false">(</mo> <mi>T</mi> <mo stretchy="false">)</mo> </mrow> </semantics></math> of silica particles and PMMA adsorbed on silica as a function of the temperature at different recovery fractions. (<b>a</b>) <math display="inline"><semantics> <mrow> <mi>θ</mi> <mo>=</mo> <mn>0</mn> <mo> </mo> <mo stretchy="false">(</mo> <mi>s</mi> <mi>i</mi> <mi>l</mi> <mi>i</mi> <mi>c</mi> <mi>a</mi> <mo> </mo> <mi>c</mi> <mi>a</mi> <mi>s</mi> <mi>e</mi> <mo stretchy="false">)</mo> </mrow> </semantics></math>, (<b>b</b>) <math display="inline"><semantics> <mrow> <mi>θ</mi> <mo>=</mo> <mn>0.31</mn> </mrow> </semantics></math>, (<b>c</b>) <math display="inline"><semantics> <mrow> <mi>θ</mi> <mo>=</mo> <mn>0.83</mn> </mrow> </semantics></math>, (<b>d</b>) <math display="inline"><semantics> <mrow> <mi>θ</mi> <mo>=</mo> <mn>1.0</mn> </mrow> </semantics></math>, and (<b>e</b>) <math display="inline"><semantics> <mrow> <mi>θ</mi> <mo>≫</mo> <mn>1</mn> <mo> </mo> <mo stretchy="false">(</mo> <mi>P</mi> <mi>M</mi> <mi>M</mi> <mi>A</mi> <mo> </mo> <mi>c</mi> <mi>a</mi> <mi>s</mi> <mi>e</mi> <mo stretchy="false">)</mo> </mrow> </semantics></math>.</p>
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17 pages, 3662 KiB  
Article
Enhancing Bi2Te2.70Se0.30 Thermoelectric Module Performance through COMSOL Simulations
by Md. Kamrul Hasan, Mehmet Ali Üstüner, Hayati Mamur and Mohammad Ruhul Amin Bhuiyan
Thermo 2024, 4(2), 185-201; https://doi.org/10.3390/thermo4020011 - 6 May 2024
Viewed by 1059
Abstract
This research employs the COMSOL Multiphysics software (COMSOL 6.2) to conduct rigorous simulations and assess the performance of a thermoelectric module (TEM) meticulously crafted with alumina (Al2O3), copper (Cu), and Bi2Te2.70Se0.30 thermoelectric (TE) materials. [...] Read more.
This research employs the COMSOL Multiphysics software (COMSOL 6.2) to conduct rigorous simulations and assess the performance of a thermoelectric module (TEM) meticulously crafted with alumina (Al2O3), copper (Cu), and Bi2Te2.70Se0.30 thermoelectric (TE) materials. The specific focus is on evaluating diverse aspects of the Bi2Te2.70Se0.30 thermoelectric generator (TEG). The TEM design incorporates Bi2Te2.70Se0.30 for TE legs of the p- and n-type positioned among the Cu layers, Cu as the electrical conductor, and Al2O3 serving as an electrical insulator between the top and bottom layers. A thorough investigation is conducted into critical parameters within the TEM, which include arc length, electric potential, normalized current density, temperature gradient, total heat source, and total net energy rate. The geometric configuration of the square-shaped Bi2Te2.70Se0.30 TEM, measuring 1 mm × 1 mm × 2.5 mm with a 0.25 mm Al2O3 thickness and a 0.125 mm Cu thickness, is scrutinized. This study delves into the transport phenomena of TE devices, exploring the impacts of the Seebeck coefficient (S), thermal conductivity (k), and electrical conductivity (σ) on the temperature differential across the leg geometry. Modeling studies underscore the substantial influence of S = ±2.41 × 10−3 V/K, revealing improved thermal conductivity and decreased electrical conductivity at lower temperatures. The findings highlight the Bi2Te2.70Se0.30 TEM’s high potential for TEG applications, offering valuable insights into design and performance considerations crucial for advancing TE technology. Full article
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Figure 1

Figure 1
<p>Standard geometry of the Bi<sub>2</sub>Te<sub>2.70</sub>Se<sub>0.30</sub> TEM (1 mm × 1 mm × 2.5 mm; copper thickness: 0.125 mm, alumina thickness: 0.250 mm).</p>
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<p>The potential difference between the hot and cold sides of Bi<sub>2</sub>Te<sub>2.70</sub>Se<sub>0.30</sub> TEM.</p>
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<p>Variation of surface temperature with electric potential for Bi<sub>2</sub>Te<sub>2.70</sub>Se<sub>0.30</sub> TEM.</p>
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<p>Variation of normalized current density with electric potential for Bi<sub>2</sub>Te<sub>2.70</sub>Se<sub>0.30</sub> TEM.</p>
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<p>Assessing the performance of various parameters for Bi<sub>2</sub>Te<sub>2.70</sub>Se<sub>0.30</sub> TEM.</p>
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<p>Seebeck coefficient for the surface of Bi<sub>2</sub>Te<sub>2.70</sub>Se<sub>0.30</sub> TEM.</p>
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<p>Seebeck coefficient for the p- and n-type legs of Bi<sub>2</sub>Te<sub>2.70</sub>Se<sub>0.30</sub> TEM.</p>
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<p>Thermal conductivity (<b>a</b>) Surface (<b>b</b>) Line graph for Bi<sub>2</sub>Te<sub>2.70</sub>Se<sub>0.30</sub> TEM.</p>
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<p>Electrical conductivity (<b>a</b>) Surface (<b>b</b>) Line graph for Bi<sub>2</sub>Te<sub>2.70</sub>Se<sub>0.30</sub> TEM.</p>
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<p>Mean figure (<b>a</b>) Surface (<b>b</b>) Line graph of merit for Bi<sub>2</sub>Te<sub>2.70</sub>Se<sub>0.30</sub> TEM.</p>
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21 pages, 2037 KiB  
Article
An Evaluation of Correlations for Predicting the Heat Transfer Coefficient during the Condensation of Saturated and Superheated Vapors Inside Channels
by Mirza M. Shah
Thermo 2024, 4(2), 164-184; https://doi.org/10.3390/thermo4020010 - 1 Apr 2024
Cited by 1 | Viewed by 1180
Abstract
Condensation heat transfer is involved in many industrial applications. Therefore, it is important to know the relative accuracy of the available methods for predicting heat transfer. Condensation can occur with saturated as well as superheated vapors. Predictive methods for both conditions were evaluated [...] Read more.
Condensation heat transfer is involved in many industrial applications. Therefore, it is important to know the relative accuracy of the available methods for predicting heat transfer. Condensation can occur with saturated as well as superheated vapors. Predictive methods for both conditions were evaluated using a wide range of data. Twelve well-known correlations for the condensation of saturated vapor, including the most recent ones, were compared with data for 51 pure fluids and mixtures from 132 sources in horizontal and vertical channels of many shapes. Channel hydraulic diameters were 0.08–49 mm, the mass flux was 1.1–1400 kg/m2s, and the reduced pressure range was 0.0006–0.949. The fluids included water, CO2, ammonia, hydrocarbons, halocarbon refrigerants, various chemicals, and heat transfer fluids. The best predictive technique was identified. The three most commonly used models for heat transfer during the condensation of superheated vapors were studied. They were first compared with test data using measured saturated condensation and forced convection heat transfer coefficients to select the best model. The selected model was then compared with test data using various correlations for heat transfer coefficients needed in the model. The best correlations to use in the model were identified. The results of this research are presented, as are recommendations for use in design. Full article
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Figure 1

Figure 1
<p>Comparison of the data of Bashar et al. (2018) [<a href="#B44-thermo-04-00010" class="html-bibr">44</a>] for saturated condensation with various correlations. R-134a in a horizontal tube: D = 2.14 mm; T<sub>SAT</sub> = 30 °C; G = 50 kg/m<sup>2</sup>s; and We<sub>GT</sub> = 22.</p>
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<p>Comparison of correlations with data of Wang and Du (2000) [<a href="#B45-thermo-04-00010" class="html-bibr">45</a>] for water in a horizontal tube: D = 3.95 mm; T<sub>SAT</sub> = 105 °C; G = 11.2 kg/m<sup>2</sup>s; and We<sub>GT</sub> = 12.</p>
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<p>Data of Goodykoontz and Dorsch (1967) [<a href="#B46-thermo-04-00010" class="html-bibr">46</a>] for water in a vertical tube compared to correlations: D = 7.44 mm; T<sub>SAT</sub> = 110 °C; and G = 265 kg/m<sup>2</sup>s.</p>
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<p>Data of Lilburne and Wood (1982) [<a href="#B47-thermo-04-00010" class="html-bibr">47</a>] for R-113 in a vertical tube compared to some correlations: D = 3.47 mm; T<sub>SAT</sub> = 52 °C; and G = 50 kg/m<sup>2</sup>s.</p>
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<p>Comparison of predictions of models for superheated vapor condensation using the measured heat transfer coefficients. Data of Kondou and Hrnjak (2012a) [<a href="#B26-thermo-04-00010" class="html-bibr">26</a>] for CO<sub>2</sub>: p<sub>r</sub> = 0.949; G = 150 kg/m<sup>2</sup>s.</p>
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<p>Comparison of the predictions of superheated condensation models using measured heat transfer coefficients. Data of Kondou and Hrnjak (2012a) [<a href="#B26-thermo-04-00010" class="html-bibr">26</a>] for R-410A: G = 100 kg/m<sup>2</sup>s; p<sub>r</sub> = 0.949.</p>
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<p>Comparison of the predictions of superheated condensation models using measured heat transfer coefficients. Data of Agarwal and Hrnjak (2015) [<a href="#B29-thermo-04-00010" class="html-bibr">29</a>] for R-1234 ze: G = 100 kg/m<sup>2</sup>s; T<sub>SAT</sub> = 50 °C.</p>
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<p>Comparison of the predictions of Model 2 using various correlations for h<sub>SAT</sub>. Data of Kondou and Hrnjak (2022a) [<a href="#B26-thermo-04-00010" class="html-bibr">26</a>] for CO<sub>2</sub>: p<sub>r</sub> = 0.949; G = 150 kg/m<sup>2</sup>s.</p>
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<p>Evaluation of Model 2 with h<sub>SAT</sub> using various correlations. Data of Fujii et al. (1978) [<a href="#B39-thermo-04-00010" class="html-bibr">39</a>] for R-113: G = 115 kg/m<sup>2</sup>s; T<sub>SAT</sub> = 50 °C.</p>
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<p>Evaluation of Model 2 with h<sub>SAT</sub> using various correlations. R-1234ze at saturation temperature of 50 °C, G = 100 kg/m<sup>2</sup>s. Data of Agarwal and Hrnjak (2015) [<a href="#B29-thermo-04-00010" class="html-bibr">29</a>]. From Shah (2023) [<a href="#B1-thermo-04-00010" class="html-bibr">1</a>].</p>
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