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17 pages, 5335 KiB  
Article
Thermophysical Modeling of the Vaporization Process in a Motive Nozzle with a Profiled Supersonic Part
by Serhii Sharapov, Danylo Husiev, Volodymyr Klymenko, Ivan Pavlenko, Dobrochna Ginter-Kramarczyk, Andżelika Krupińska, Marek Ochowiak and Sylwia Włodarczak
Energies 2024, 17(24), 6465; https://doi.org/10.3390/en17246465 (registering DOI) - 22 Dec 2024
Viewed by 48
Abstract
In this article, thermophysical modeling of boiling flows in the motive nozzle is carried out for a liquid–vapor jet apparatus (LVJA). Existing thermophysical models make it possible to calculate nozzles, which, in their shape, are close to Laval nozzles. They also allow for [...] Read more.
In this article, thermophysical modeling of boiling flows in the motive nozzle is carried out for a liquid–vapor jet apparatus (LVJA). Existing thermophysical models make it possible to calculate nozzles, which, in their shape, are close to Laval nozzles. They also allow for determining the position of the outlet cross-sectional area of the nozzle, where the flow separation from the channel walls occurs. However, these models do not allow for profiling the nozzle’s supersonic part, which does not make it possible to ensure the maximum efficiency of the vaporization process. Therefore, in the presented article, the available thermophysical model was improved significantly, which made it possible to obtain the profile of the supersonic part of the nozzle. As a result, a geometric shape that ensures the highest efficiency of the outflow process can be chosen for the primary flow at specified initial and final thermodynamic parameters. According to the calculation results and the proposed methodology, parameters were distributed along the nozzle for the primary flow. Also, efficiency indicators of the outflow of the boiling liquid underheated to saturation were achieved for the different geometric shapes. Mathematical modeling of the operating process in the motive nozzle using ANSYS CFX 2004 R1 (ANSYS, Inc., Canonsburg, PA, USA) was performed to prove the reliability of the results. Also, a comparative analysis of the obtained calculation and simulation results for nozzles with a profiled supersonic part and straight walls was carried out. To assess the expediency of profiling the supersonic part of the nozzle for the primary flow at the LVJA, a comparison of analytical modeling and numerical simulation results with the experimental studies was carried out for nozzles with straight walls. Finally, the velocity ratios of nozzles with profiled supersonic parts and straight walls were obtained. This allowed for rational choosing of the nozzle shape to ensure the highest vaporization efficiency. Full article
(This article belongs to the Section K: State-of-the-Art Energy Related Technologies)
Show Figures

Figure 1

Figure 1
<p>Geometric features of motive nozzles with different geometries of the supersonic part: (<b>a</b>) conical shape; (<b>b</b>) parabolic shape; (<b>c</b>) hyperbolic shape; (<b>d</b>) elliptical shape; (<b>e</b>) Vitoshynskyi shape.</p>
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<p>Calculation grid for a nozzle with a parabolic shape of the supersonic part (<a href="#energies-17-06465-f001" class="html-fig">Figure 1</a>b).</p>
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<p>The design scheme of the vaporization process in a motive nozzle: “<span class="html-italic">f</span>–<span class="html-italic">a</span>”—the supersonic part of the nozzle: <span class="html-italic">f</span>, <span class="html-italic">v</span>, and <span class="html-italic">c</span>—the 1st, 2nd, and 3rd critical sections, respectively; *, **, and ***—real positions of the 1st, 2nd, and 3rd critical sections, respectively.</p>
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<p>Experimental stand: (<b>a</b>)—general view; (<b>b</b>)—the conical supersonic part of the motive nozzle.</p>
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<p>Pressure changes along the conical (<b>a</b>), parabolic (<b>b</b>), hyperbolic (<b>c</b>), elliptic (<b>d</b>), and Vitoshynskyi (<b>e</b>) shapes of the nozzle according to the mode parameters presented in <a href="#energies-17-06465-t001" class="html-table">Table 1</a>.</p>
Full article ">Figure 6
<p>The numerical and experimental results for pressure changes along the conical (<b>a</b>) (■), parabolic (<b>b</b>) (▲), hyperbolic (<b>c</b>) (●), elliptic (<b>d</b>) (◆), and Vitoshynskyi (<b>e</b>) (○) shapes according to the mode parameters presented in <a href="#energies-17-06465-t001" class="html-table">Table 1</a> (“- - -”—CFD simulation results, “---”—calculation results according to the proposed methodology, “✕✕✕”—experimental results for a nozzle with the conical shape).</p>
Full article ">Figure 6 Cont.
<p>The numerical and experimental results for pressure changes along the conical (<b>a</b>) (■), parabolic (<b>b</b>) (▲), hyperbolic (<b>c</b>) (●), elliptic (<b>d</b>) (◆), and Vitoshynskyi (<b>e</b>) (○) shapes according to the mode parameters presented in <a href="#energies-17-06465-t001" class="html-table">Table 1</a> (“- - -”—CFD simulation results, “---”—calculation results according to the proposed methodology, “✕✕✕”—experimental results for a nozzle with the conical shape).</p>
Full article ">Figure 7
<p>Velocity changes along the conical (<b>a</b>), parabolic (<b>b</b>), hyperbolic (<b>c</b>), elliptic (<b>d</b>), and Vitoshynskyi (<b>e</b>) shapes of the nozzle according to the mode parameters presented in <a href="#energies-17-06465-t001" class="html-table">Table 1</a>.</p>
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<p>The numerical and experimental results for velocity changes along the conical (<b>a</b>) (■), parabolic (<b>b</b>) (▲), hyperbolic (<b>c</b>) (●), elliptic (<b>d</b>) (◆), and Vitoshynskyi (<b>e</b>) (○) shapes according to the mode parameters presented in <a href="#energies-17-06465-t001" class="html-table">Table 1</a> (“- - -”—CFD simulation results, “---”—calculation results according to the proposed methodology, “✕✕✕”—experimental results for a nozzle with the conical shape).</p>
Full article ">Figure 8 Cont.
<p>The numerical and experimental results for velocity changes along the conical (<b>a</b>) (■), parabolic (<b>b</b>) (▲), hyperbolic (<b>c</b>) (●), elliptic (<b>d</b>) (◆), and Vitoshynskyi (<b>e</b>) (○) shapes according to the mode parameters presented in <a href="#energies-17-06465-t001" class="html-table">Table 1</a> (“- - -”—CFD simulation results, “---”—calculation results according to the proposed methodology, “✕✕✕”—experimental results for a nozzle with the conical shape).</p>
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<p>Evaluated efficiency for nozzles with a diffuser part of conical (■; blue line), parabolic (▲; red line), hyperbolic (●; yellow line), elliptic (◆; black line), and Vitoshynskyi (○; green line) shapes vs. relative initial underheating.</p>
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12 pages, 19896 KiB  
Communication
Communication Link Analysis of a Low-Earth Orbit Satellites Considering Interference Sources Moving Along Various Parabola-Curved Paths
by Hyunmu Kang, Eunjung Kang and Hosung Choo
Sensors 2024, 24(24), 8185; https://doi.org/10.3390/s24248185 (registering DOI) - 21 Dec 2024
Viewed by 376
Abstract
We analyze the communication link of an LEO satellite considering interference sources moving along various parabola-curved paths. In this situation, the location of the ground station, airborne interference source paths, and the satellite’s trajectory were expressed in the East-North-Up (ENU) coordinate system. The [...] Read more.
We analyze the communication link of an LEO satellite considering interference sources moving along various parabola-curved paths. In this situation, the location of the ground station, airborne interference source paths, and the satellite’s trajectory were expressed in the East-North-Up (ENU) coordinate system. The airborne interference source path is designed using a parabola equation with a directrix parallel to the satellite’s trajectory to analyze the interference situation for more diverse interference source paths, rather than using a straight path. To investigate critical interference situations where the J/S ratio is maintained above −20 dB with a small deviation during the communication time, we investigate interference situations by changing the parameters of the interference source path. The genetic algorithm (GA) is used to easily find an airborne interference source path that maintains the J/S ratio above −20 dB with a small deviation. A cost function for the GA is then defined as the average difference between the J/S ratio and the reference value (−10 dB and −20 dB) during the communication time. The optimum parameters of the interference source path are determined at a minimum cost in the GA. These results demonstrate that more significant interference situations for the communication link can be easily found by using parabola-curved paths and the GA. As a result, previous studies investigated the basic tendency of the J/S ratio using straight paths. However, this study provides a database for operating an anti-jamming system based on the obtained optimized path. Full article
(This article belongs to the Section Remote Sensors)
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Figure 1

Figure 1
<p>LEO satellite communication link under the interference situation based on the ENU coordinate system.</p>
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<p>Parabola equations for the airborne interference source path based on the ENU coordinate system.</p>
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<p>The LEO satellite communication link analysis for the parabola-curved and straight paths of the airborne interference source according to the variation in p (when <span class="html-italic">d<sub>v</sub></span> = 15 km, <span class="html-italic">h<sub>i</sub></span> = 9 km, and <span class="html-italic">v<sub>i</sub></span> = 400 km/h): (<b>a</b>) parabola-curved and straight paths of the interference source on geodetic coordinates map; (<b>b</b>) <span class="html-italic">d<sub>i</sub></span> of the interference source at an altitude of <span class="html-italic">h<sub>i</sub></span>; (<b>c</b>) 3D radiation pattern of the ground station antenna in UV domain; (<b>d</b>) 2D radiation pattern of the ground station antenna; (<b>e</b>) side-lobe gain of the ground station antenna with the regression model; (<b>f</b>) side-lobe gain of the ground station antenna according to airborne interference paths; (<b>g</b>) results of the <span class="html-italic">J</span>/<span class="html-italic">S</span> ratio according to focal point <span class="html-italic">p</span>.</p>
Full article ">Figure 3 Cont.
<p>The LEO satellite communication link analysis for the parabola-curved and straight paths of the airborne interference source according to the variation in p (when <span class="html-italic">d<sub>v</sub></span> = 15 km, <span class="html-italic">h<sub>i</sub></span> = 9 km, and <span class="html-italic">v<sub>i</sub></span> = 400 km/h): (<b>a</b>) parabola-curved and straight paths of the interference source on geodetic coordinates map; (<b>b</b>) <span class="html-italic">d<sub>i</sub></span> of the interference source at an altitude of <span class="html-italic">h<sub>i</sub></span>; (<b>c</b>) 3D radiation pattern of the ground station antenna in UV domain; (<b>d</b>) 2D radiation pattern of the ground station antenna; (<b>e</b>) side-lobe gain of the ground station antenna with the regression model; (<b>f</b>) side-lobe gain of the ground station antenna according to airborne interference paths; (<b>g</b>) results of the <span class="html-italic">J</span>/<span class="html-italic">S</span> ratio according to focal point <span class="html-italic">p</span>.</p>
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<p>The LEO satellite communication link analysis for the other case of interference situations with various airborne interference source paths, according to <span class="html-italic">p</span> (when <span class="html-italic">d<sub>v</sub></span> = 25 km, <span class="html-italic">h<sub>i</sub></span> = 12 km, and <span class="html-italic">v<sub>i</sub></span> = 850 km/h): (<b>a</b>) parabola curved and straight paths of the interference source on geodetic coordinates map; (<b>b</b>) results of <span class="html-italic">J</span>/<span class="html-italic">S</span> ratios according to <span class="html-italic">p</span>.</p>
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<p>Flowchart of the GA to find the airborne interference source paths that have the smallest deviation in the <span class="html-italic">J</span>/<span class="html-italic">S</span> ratio.</p>
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<p>Optimized and straight paths of the airborne interference source when <span class="html-italic">JSR<sub>ref</sub></span> = −10 dB: (<b>a</b>) optimized and straight paths on geodetic coordinates map; (<b>b</b>) results of the <span class="html-italic">J</span>/<span class="html-italic">S</span> ratio of the optimized and straight paths.</p>
Full article ">Figure 7
<p>Optimized and straight paths when <span class="html-italic">JSR<sub>ref</sub></span> = −20 dB: (<b>a</b>) optimized and straight paths on geodetic coordinates map; (<b>b</b>) results of the <span class="html-italic">J</span>/<span class="html-italic">S</span> ratio of the optimized and straight paths.</p>
Full article ">
16 pages, 1332 KiB  
Article
Characterization of Several 2-Ethylhexyl Nitrates with Vegetable Oil (Castor or Sunflower Oil) Blends in Triple Blends with Diesel, Working as Advanced Biofuels in C.I. Diesel Engines
by Rafael Estevez, Francisco J. López-Tenllado, Vicente Montes, Antonio A. Romero, Felipa M. Bautista and Diego Luna
Appl. Sci. 2024, 14(24), 11968; https://doi.org/10.3390/app142411968 (registering DOI) - 20 Dec 2024
Viewed by 284
Abstract
This study evaluates the performance of biofuels created from triple blends of fossil diesel, sunflower or castor oil (SVOs), and 2-Ethylhexyl Nitrate (EHN), a low-viscosity, high-cetane (LVHC) solvent. EHN reduces the viscosity of SVOs to enable their use in conventional diesel engines without [...] Read more.
This study evaluates the performance of biofuels created from triple blends of fossil diesel, sunflower or castor oil (SVOs), and 2-Ethylhexyl Nitrate (EHN), a low-viscosity, high-cetane (LVHC) solvent. EHN reduces the viscosity of SVOs to enable their use in conventional diesel engines without compromising fuel properties. The results show that the power output from these blends is similar to or greater than that of fossil diesel, with comparable fuel consumption. Furthermore, the blends significantly reduce emissions of carbon monoxide (CO) and soot, though NOx emissions are slightly higher due to the nitrogen content in EHN. However, NOx levels remain within permissible limits. The substitution of fossil diesel could be further enhanced if EHN were produced using green hydrogen and lignocellulosic biomass, making it a renewable and sustainable biofuel component. These findings support the potential of EHN/SVO biofuel blends to replace a significant portion of fossil diesel in conventional diesel engines while maintaining performance and reducing harmful emissions, except for a slight increase in NOx. Full article
(This article belongs to the Special Issue Bioenergy and Bioproducts from Biomass and Waste)
13 pages, 730 KiB  
Article
Newton’s First Law and the Grand Unification
by Martin Tamm
Symmetry 2024, 16(12), 1694; https://doi.org/10.3390/sym16121694 (registering DOI) - 20 Dec 2024
Viewed by 176
Abstract
This paper is devoted to the study of stationary trajectories of free particles. From a classical point of view, this appears to be an almost trivial problem: Free particles should follow straight lines as predicted by Newton’s first law, and straight lines are [...] Read more.
This paper is devoted to the study of stationary trajectories of free particles. From a classical point of view, this appears to be an almost trivial problem: Free particles should follow straight lines as predicted by Newton’s first law, and straight lines are indeed the stationary trajectories of the standard action integrals in the classical theory. In the following, however, a general relativistic approach is studied, and in this situation it is much less evident what action integral should be used. As it turns out, using the traditional Einstein–Hilbert principle gives us stationary states very much in line with the classical theory. But it is suggested that a different action principle, and in fact one which is closer to quantum mechanics, gives stationary states with a much richer structure: Even if these states in a sense can represent particles which obey the first law, they are also inherently rotating. Although we may still be far from understanding how general relativity and quantum mechanics should be united, this may give an interesting clue to why rotation (or rather spin, which is a different but related concept) seems to be the natural state of motion for elementary particles. Full article
(This article belongs to the Section Physics)
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Figure 1

Figure 1
<p>To the left, a very schematic illustration of a perturbation of the standard metric on Euclidean three-space (although by necessity drawn in two dimensions), which circulates with time around an axis in space (to the right).</p>
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<p>The solutions to the equation <math display="inline"><semantics> <mrow> <msup> <mi>c</mi> <mrow> <mo>*</mo> <mo>*</mo> </mrow> </msup> <mrow> <mo>(</mo> <mi>b</mi> <mo>,</mo> <mi>d</mi> <mo>)</mo> </mrow> <mo>=</mo> <mn>0</mn> </mrow> </semantics></math> for <math display="inline"><semantics> <mrow> <mi>d</mi> <mo>&gt;</mo> <mn>0</mn> </mrow> </semantics></math>.</p>
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<p>A schematic illustration of a classical string (to the left). To the right, the same string rotating around an axis in space (not in time).</p>
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<p>A schematic illustration of such a classical photon, as in the text.</p>
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35 pages, 11125 KiB  
Article
Analysis of Static Aeroelastic Characteristics of Distributed Propulsion Wing
by Junlei Sun, Zhou Zhou, Tserendondog Tengis and Huailiang Fang
Aerospace 2024, 11(12), 1045; https://doi.org/10.3390/aerospace11121045 - 20 Dec 2024
Viewed by 248
Abstract
The static aeroelastic characteristics of the distributed propulsion wing (DPW) were studied using the CFD/CSD loose coupling method in this study. The momentum source method of the Reynolds-averaged Navier–Stokes equation based on the k-ω SST turbulence model solution was used as the CFD [...] Read more.
The static aeroelastic characteristics of the distributed propulsion wing (DPW) were studied using the CFD/CSD loose coupling method in this study. The momentum source method of the Reynolds-averaged Navier–Stokes equation based on the k-ω SST turbulence model solution was used as the CFD solution module. The upper and lower surfaces of the DPW were established using the cubic B-spline basis function method, and the surfaces of the inlet and outlet were established using the fourth-order Bezier curve. Finally, a three-dimensional parametric model of the DPW was established. A structural finite-element model of the DPW was established, a multipoint array method program based on the three-dimensional radial basis function (RBF) was written as a data exchange module to realize the aerodynamic and structural data exchange of the DPW’s static aeroelastic analysis process, and, finally, an aeroelastic analysis of the DPW was achieved. The results show that the convergence rate of the CFD/CSD loosely coupled method is fast, and the structural static aeroelastic deformation is mainly manifested as bending deformation and positive torsion deformation, which are typical static aeroelastic phenomena of the straight wing. Under the influence of static aeroelastic deformation, the increase in the lift characteristics of the DPW is mainly caused by the slipstream region of the lower surface and the non-slipstream region of the upper and lower surface. Meanwhile, the increase in its nose-up moment and the increase in the longitudinal static stability margin may have an impact on the longitudinal stability of the UAV. To meet the requirements of engineering applications, a rapid simulation method of equivalent airfoil, which can be applied to commercial software for analysis, was developed, and the effectiveness of the method was verified via comparison with the CFD/CSD loose coupling method. On this basis, the static aeroelastic characteristics of the UAV with DPWs were studied. The research results reveal the static aeroelastic characteristics of the DPW, which hold some significance for engineering guidance for this kind of aircraft. Full article
(This article belongs to the Section Aeronautics)
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Figure 1

Figure 1
<p>The configuration diagram and main components of the DPW.</p>
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<p>The flow chart of the static aeroelastic analysis of the DPW.</p>
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<p>Schematic of the momentum source method grid and the MRF method grid. (<b>a</b>) Schematic diagram of the momentum source method grid; (<b>b</b>) Schematic diagram of the MRF method grid.</p>
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<p>Comparison of numerical simulation between the momentum source method and the MRF method.</p>
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<p>Schematic of the automatically generated unstructured surface grid for the DPW after deformation.</p>
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<p>Structural finite-element model of the DPW.</p>
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<p>Schematic of fluid–structure coupling loading effect.</p>
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<p>The control section position and control parameters of the DPW.</p>
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<p>The DPW inlet modeling diagram.</p>
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<p>Schematic of the parametrized DPW model.</p>
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<p>The iterative convergence curve.</p>
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<p>Cloud diagram of DPW bending and torsion deformation in convergence state (α = 4°).</p>
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<p>Bending and torsional deformation spanwise distribution of DPW.</p>
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<p>Comparison of aerodynamic characteristics before and after static aeroelastic deformation.</p>
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<p>The pressure distribution of the upper and lower surfaces.</p>
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<p>Schematic of section locations.</p>
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<p>Pressure distribution of the DPW’s upper surface (α = 0°).</p>
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<p>Pressure distribution curve of the DPW’s lower surface (α = 0°).</p>
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<p>Static aeroelastic deformation under the influence of thrust (α = 0°).</p>
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<p>Schematic of aerodynamic grid and the combination airfoil.</p>
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<p>Comparison of life coefficient and pitch moment coefficient of the DPW and the wing with the combined airfoil.</p>
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<p>Diagram of the unit and the span lift distribution of the DPW units.</p>
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<p>Pressure distribution and pitching moment calculation of an airfoil.</p>
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<p>Schematic of two-dimensional grid automatically generated before and after airfoil deformation.</p>
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<p>Comparison of airfoil before and after optimization.</p>
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<p>Comparison of lift coefficient and pitch moment coefficient between the wing using the equivalent airfoil and the DPW.</p>
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<p>Static aeroelastic analysis of the DPW using the equivalent airfoil rapid simulation method.</p>
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<p>Comparison of bending deformation and torsional deformation of DPW.</p>
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<p>Configuration of UAV with DPWs.</p>
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<p>Structural finite-element model of the UAV with the DPWs and its dipole aerodynamic grid diagram.</p>
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<p>Longitudinal static stability variation diagram.</p>
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<p>Displacement cloud diagrams.</p>
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<p>Control surface efficiency curve.</p>
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14 pages, 4138 KiB  
Article
Use of Spectral Clustering for Identifying Circulation Patterns of the East Korea Warm Current and Its Extension
by Eun Young Lee, Dong Eun Lee, Hye-Ji Kim, Haedo Baek, Young Ho Kim and Young-Gyu Park
J. Mar. Sci. Eng. 2024, 12(12), 2338; https://doi.org/10.3390/jmse12122338 - 20 Dec 2024
Viewed by 289
Abstract
A graphical clustering approach was used to objectively identify prevalent surface circulation patterns in the East/Japan Sea (EJS). By applying a spectral clustering algorithm, three distinct patterns in the East Korea Warm Current (EKWC) and its extension were identified from daily maps of [...] Read more.
A graphical clustering approach was used to objectively identify prevalent surface circulation patterns in the East/Japan Sea (EJS). By applying a spectral clustering algorithm, three distinct patterns in the East Korea Warm Current (EKWC) and its extension were identified from daily maps of reanalyzed sea surface heights spanning the past 30 years. The results are consistent with previous studies that used manual classification of the EKWC’s Lagrangian trajectories, highlighting the effectiveness of spectral clustering in accurately characterizing the surface circulation states in the EJS. Notably, the recent dominance of northern paths, as opposed to routes along Japan’s coastline or those departing from Korea’s east coast further south, has prompted focused re-clustering of the northern paths according to their waviness. This re-clustering, with additional emphasis on path length, distinctly categorized two patterns: straight paths (SPs) and large meanders (LMs). Notably, SPs have become more prevalent in the most recent years, while LMs have diminished. An autoregression analysis reveals that seasonal anomalies in the cluster frequency in spring tend to persist through to the following autumn. The frequency anomalies in the SPs correlate strongly with the development of pronounced anomalies in the gradient of meridional sea surface height and negative anomalies in the surface wind stress curl in the preceding cold seasons. This relationship explains the observed correlation between a negative Arctic Oscillation during the preceding winter and the increased frequency of SPs in the subsequent spring. The rapid increase in the occurrence of SPs indicates that a reduction in LMs limits the mixing of cold, fresh, northern waters with warm, saline, southern waters, thereby reinforcing the presence of SPs due to a strengthened gradient of meridional surface height and contributing to a slowdown in the regional overturning circulation. Full article
(This article belongs to the Section Physical Oceanography)
Show Figures

Figure 1

Figure 1
<p>Three clusters of the East Korea Warm Current (EKWC)’s paths based on the spectral clustering analysis. The intensity of black indicates the density of the paths in each cluster (<b>a</b>–<b>c</b>), with darker areas representing more frequent paths in these specific locations. (<b>d</b>–<b>f</b>) show the yearly counts of the EKWC’s paths across the 30-year period. The labeled seasons indicate their primary appearance. N indicates the frame count.</p>
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<p>The zonal mean sea surface height (SSH) and zonal geostrophic current derived from the sea surface distribution in the East/Japan Sea (EJS).</p>
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<p>Monthly mean average speed of the current across the western channel of the Korea Strait. Black indicates the climatological means, red the average at the timing of the Inertial Boundary Current (IBC), blue the average at the Ulleung Eddy (UE), and green the average at the Tsushima Warm Current (TWC). The light gray shading indicates ±1 standard deviation gtom the climatological means.</p>
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<p>Two sub-clusters of the IBC—(<b>a</b>) large meanders (LMs) and (<b>b</b>) straight paths (SPs)—with colored shading indicating the path frequency at each grid point. (<b>c</b>,<b>d</b>) exhibit the yearly counts of LMs and SPs, respectively. (<b>e</b>,<b>f</b>) show the relative occurrence of each cluster with respect to the number of occurrences of the IBC.</p>
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<p>Monthly autocorrelation of relative occurrence of SPs, marked with asterisks for significance at 95%.</p>
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<p>Composite-averaged zonal mean of the seasonal temperature anomalies in the EJS associated with the index of the relative occurrence of SPs in (<b>a</b>) January–February–March, (<b>b</b>) April–May–June, (<b>c</b>) July–August–September, and (<b>d</b>) October–November–December. The black vertical line indicates the mean location of the SP axis. Sections are stippled if they are significantly different from the population mean according to Student’s <span class="html-italic">t</span>-test at 95%.</p>
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<p>Winter (December–January–February) mean Arctic Oscillation (AO) index in red and Pacific Decadal Oscillation (PDO) index in blue, overlaid onto the relative occurrence of straight paths and large meanders in the late spring (April–May–June), presented using green and yellow bars, respectively. The Spearman’s correlation coefficients of the relative occurrence of SPs with the two climate indices presented are 0.23 for PDO and −0.54 for AO, which is marked with an asterisk for significance at 95%.</p>
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<p>(<b>a</b>) Linear regression coefficients of the zonal mean of the seasonal temperature anomalies in the EJS with the standardized mean negative AO index for DJF. Stippled at 95% significance according to Student’s <span class="html-italic">t</span>-test. (<b>b</b>) The zonal mean average sea surface height (SSH), with the value at the center of the mean IBC axis subtracted and composite-averaged with SPs in red and LMs in gray and the mean of the IBC dashed in black. Overlaid in blue is the linear regression coefficient for the anomalies in the zonal mean surface wind averaged in DJFMA with the standardized mean negative AO index for DJF.</p>
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<p>Linear regression coefficients of the EJS’s meridional overturning circulation with the index of the SP count. Stippled at 95% significance according to Student’s <span class="html-italic">t</span>-test.</p>
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25 pages, 8903 KiB  
Article
Mesh Stiffness and Dynamic Modeling and Analysis of Modified Straight Bevel Gears
by Ding Zhang, Ze-Hua Hu, Wen-Tao Liu, Jin-Yuan Tang, Zhou Sun and Zhao-Yang Tian
Appl. Sci. 2024, 14(24), 11919; https://doi.org/10.3390/app142411919 - 19 Dec 2024
Viewed by 344
Abstract
Gear modification, which involves the removal of material from the theoretical surface to improve the contact characteristics of the gear face, is widely applied in gear vibration reduction and noise optimization design. This paper establishes a dynamic model of the straight bevel gear [...] Read more.
Gear modification, which involves the removal of material from the theoretical surface to improve the contact characteristics of the gear face, is widely applied in gear vibration reduction and noise optimization design. This paper establishes a dynamic model of the straight bevel gear (SBG) transmission system to accurately and efficiently evaluate the effects of different modification strategies on the vibrational characteristics of SBGs. Initially, the time-varying meshing stiffness (TVMS) of standard SBGs was calculated, and methods such as the slicing method and deformation coordination equations were used to calculate the TVMS under tooth profile modification (TPM), Lead crown relief (LCR), and comprehensive modification (CM), which were then validated against finite element method (FEM) calculations. Subsequently, taking into account the impact of time-varying meshing point vectors and the degree of contact overlap, a finite element node dynamic model of the SBG transmission system was established. Finally, by comparing the dynamic characteristics under different modification conditions, the study further elucidates that selecting the appropriate modification method and amount according to different service scenarios is an effective means to suppress gear transmission vibration. This research provides a theoretical basis for the design of gear modification and vibration control for SBGs. Full article
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<p>Principle of tooth surface formation for straight bevel gears.</p>
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<p>Schematic diagram of tooth surface rotation treatment.</p>
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<p>Schematic diagram of contact analysis.</p>
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<p>Slicing the straight bevel gear.</p>
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<p>Straight bevel gear.</p>
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<p>Calculation procedure of TVMS for a straight bevel gear pair with CM.</p>
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<p>Finite element model of meshing gears.</p>
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<p>TVMS of Straight Bevel Gears. (<b>a</b>) gear pair 1. (<b>b</b>) gear pair 2.</p>
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<p>TVMS considering the LCR of Straight Bevel Gears. (<b>a</b>) gear pair 1. (<b>b</b>) gear pair 2.</p>
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<p>TVMS considering the tooth profile modification of Straight Bevel Gears. (<b>a</b>) gear pair 1. (<b>b</b>) gear pair 2.</p>
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<p>TVMS considering the CMs of Straight Bevel Gears. (<b>a</b>) gear pair 1. (<b>b</b>) gear pair 2.</p>
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<p>Illustration of bevel gear transmission system.</p>
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<p>Element model of gear rotor.</p>
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<p>Straight bevel gear pair.</p>
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<p>Element model of the shaft element.</p>
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<p>DTE of TPM.</p>
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<p>DTE of LCR.</p>
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<p>DTE of CM.</p>
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19 pages, 18317 KiB  
Article
A Study on the Impact Toughness of the Simulated Heat-Affected Zone in Multi-Layer and Multi-Pass Welds of 1000 MPa Grade Steel for Hydroelectric Applications
by Yuwei Li, Yuanbo Li and Jianxiu Chang
Metals 2024, 14(12), 1455; https://doi.org/10.3390/met14121455 - 19 Dec 2024
Viewed by 278
Abstract
The microstructure and impact toughness of a steel material subjected to multi-layer and multi-pass welding with varying secondary peak temperatures were investigated using welding thermal simulation. The detailed microstructures and fracture morphologies were examined by SEM, TEM, and EBSD. When the secondary peak [...] Read more.
The microstructure and impact toughness of a steel material subjected to multi-layer and multi-pass welding with varying secondary peak temperatures were investigated using welding thermal simulation. The detailed microstructures and fracture morphologies were examined by SEM, TEM, and EBSD. When the secondary peak temperature reaches 650 °C, the microstructure resembles that of a primary thermal cycle at 1300 °C, characterized by coarse grains and straight grain boundaries. As the temperature increases to 750 °C, chain-like structures of bulky M/A (martensite/austenite) constituents form at grain boundaries, widening them significantly. At 850 °C, grain boundaries become discontinuous, and large bulky M/A constituents disappear. At 1000 °C, smaller austenitic grains form granular bainite during cooling. However, at 1200 °C, grain coarsening occurs due to the significant increase in peak temperature, accompanied by a lath martensite structure at higher cooling rates. In terms of toughness, the steel exhibits better toughness at 850 °C and 1000 °C, with ductile fracture characteristics. Conversely, at 650 °C, 750 °C, and 1200 °C, the steel shows brittle fracture features. Microscopically, the fracture surfaces at these temperatures exhibit quasi-cleavage fracture characteristics. Notably, chain-like M/A constituents at grain boundaries significantly affect impact toughness and are the primary cause of toughness deterioration in the intercritical coarse-grained heat-affected zone. Full article
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<p>The schematic of the sample orientation.</p>
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<p>Thermal simulation curves at different secondary peak temperatures.</p>
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<p>Microstructure of the base material: (<b>a</b>) OM; (<b>b</b>) SEM; (<b>c</b>) TEM.</p>
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<p>The F<sub>m</sub> values of the test steel at −40 °C under different secondary thermal cycle peak temperatures.</p>
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<p>The impact absorption energy of the test steel at −40 °C under different secondary thermal cycle peak temperatures.</p>
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<p>The load–displacement curves of the test steel at −40 °C under different secondary thermal cycle peak temperatures.</p>
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<p>Impact fracture morphology of test steel at different peak temperatures of one thermal cycle: (<b>a</b>) 650 °C; (<b>b</b>) 750 °C; (<b>c</b>) 850 °C; (<b>d</b>) 1000 °C; (<b>e</b>) 1200 °C.</p>
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<p>OM and SEM microstructure of steel at different peak temperatures of secondary thermal cycles: (<b>a</b>,<b>a’</b>,<b>a”</b>): 650 °C; (<b>b</b>,<b>b’</b>,<b>b”</b>): 750 °C; (<b>c</b>,<b>c’</b>,<b>c”</b>): 850 °C; (<b>d</b>,<b>d’</b>,<b>d”</b>): 1000 °C; (<b>e</b>,<b>e’</b>,<b>e”</b>): 1200 °C. The grain boundaries were marked with yellow lines.</p>
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<p>TEM of the tested steel after a secondary thermal cycle with a peak temperature of 650 °C: (<b>a</b>) elongated lath bundles; (<b>b</b>) high-density dislocations; (<b>c</b>) carbides.</p>
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<p>TEM of the tested steel after a secondary thermal cycle with a peak temperature of 750 °C: (<b>a</b>) elongated lath bundles; (<b>b</b>) blocky M/A at grain boundary. The outline of M/A constituent was marked with yellow line; (<b>c</b>) carbides.</p>
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<p>TEM of the tested steel after a secondary thermal cycle with a peak temperature of 850 °C: (<b>a</b>) grain morphology; (<b>b</b>) blurred lath edges; (<b>c</b>) carbides.</p>
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<p>TEM of the tested steel after a secondary thermal cycle with a peak temperature of 1000 °C. (<b>a</b>) Lath bundles arranged in multiple orientations; (<b>b</b>) blurred lath edges; (<b>c</b>) carbides.</p>
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<p>TEM of the tested steel after a secondary thermal cycle with a peak temperature of 1200 °C: (<b>a</b>) lath morphologies; (<b>b</b>) carbides; (<b>c</b>) blurred lath edges.</p>
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<p>EBSD results (GB, KAM, IPF) at different peak temperatures: (<b>a</b>,<b>a’</b>,<b>a”</b>): 650 °C; (<b>b</b>,<b>b’</b>,<b>b”</b>): 750 °C; (<b>c</b>,<b>c’</b>,<b>c”</b>): 850 °C; (<b>d</b>,<b>d’</b>,<b>d”</b>): 1000 °C; (<b>e</b>,<b>e’</b>,<b>e”</b>): 1200 °C.</p>
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<p>EBSD results (GB, KAM, IPF) at different peak temperatures: (<b>a</b>,<b>a’</b>,<b>a”</b>): 650 °C; (<b>b</b>,<b>b’</b>,<b>b”</b>): 750 °C; (<b>c</b>,<b>c’</b>,<b>c”</b>): 850 °C; (<b>d</b>,<b>d’</b>,<b>d”</b>): 1000 °C; (<b>e</b>,<b>e’</b>,<b>e”</b>): 1200 °C.</p>
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<p>Results of parent phase grain reconstruction for the tested steel at different peak temperatures of secondary thermal cycles: (<b>a</b>) 650 °C; (<b>b</b>) 750 °C; (<b>c</b>) 850 °C; (<b>d</b>) 1000 °C; (<b>e</b>) 1200 °C.</p>
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<p>Crystallographic analysis results of the tested steel at different peak temperatures of secondary thermal cycles: (<b>a</b>) grain size; (<b>b</b>) grain boundary misorientation; (<b>c</b>) grain boundary misorientation; (<b>d</b>) local misorientations.</p>
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21 pages, 5596 KiB  
Article
Research on Path-Following Technology of a Single-Outboard-Motor Unmanned Surface Vehicle Based on Deep Reinforcement Learning and Model Predictive Control Algorithm
by Bin Cui, Yuanming Chen, Xiaobin Hong, Hao Luo and Guanqiao Chen
J. Mar. Sci. Eng. 2024, 12(12), 2321; https://doi.org/10.3390/jmse12122321 - 18 Dec 2024
Viewed by 395
Abstract
Path following is one of the key technologies for unmanned surface vehicles (USVs). This paper proposes a path-tracking control method for a single-outboard-motor USV based on a Deep Deterministic Policy Gradient (DDPG) algorithm and model predictive control (MPC) algorithm. Initially, the motion model [...] Read more.
Path following is one of the key technologies for unmanned surface vehicles (USVs). This paper proposes a path-tracking control method for a single-outboard-motor USV based on a Deep Deterministic Policy Gradient (DDPG) algorithm and model predictive control (MPC) algorithm. Initially, the motion model and outboard motor model of the USV are analyzed. Subsequently, simulation and real ship experiments provide a comprehensive performance comparison between the proposed DDPG-MPC method and the traditional ALOS-PID method. The results indicate that for straight path tracking, the DDPG-MPC algorithm achieves 37% and 21% reductions in the average cross error and heading angle error, respectively, compared to the ALOS-PID algorithm. The real ship experiments further validate the DDPG-MPC algorithm’s advantages in real-world environments. Specifically, under disturbances like wind, waves, and currents, the maximum cross error of the DDPG-MPC algorithm is one-third of the ALOS-PID algorithm. Additionally, the DDPG-MPC algorithm sustains a higher and more stable longitudinal velocity over extended periods, while the ALOS-PID algorithm shows greater instability and variability. Overall, the findings confirm the feasibility and effectiveness of the proposed approach, highlighting its potential for enhancing path-tracking control performance in single-outboard-motor USVs. Full article
(This article belongs to the Section Ocean Engineering)
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<p>Coordinate system for kinematic modeling of USV.</p>
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<p>Algorithm framework for path-following control of single-outboard-motor USV.</p>
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<p>The reward function. (<b>a</b>) The reward function <math display="inline"><semantics> <mrow> <msub> <mi>r</mi> <mi>ε</mi> </msub> </mrow> </semantics></math> related to the cross-track error <math display="inline"><semantics> <mi>ε</mi> </semantics></math> between the USV’s actual position and the desired tracking path. (<b>b</b>) The reward function <math display="inline"><semantics> <mrow> <msub> <mi>r</mi> <mi>β</mi> </msub> </mrow> </semantics></math> related to the deviation <math display="inline"><semantics> <mi>β</mi> </semantics></math> between the USV’s heading angle and the desired path angle. (<b>c</b>) The reward function <math display="inline"><semantics> <mrow> <msub> <mi>r</mi> <mrow> <mo>Δ</mo> <msub> <mi>ψ</mi> <mi>d</mi> </msub> </mrow> </msub> </mrow> </semantics></math> related to the change in the desired heading angle <math display="inline"><semantics> <mrow> <mo>Δ</mo> <msub> <mi>ψ</mi> <mi>d</mi> </msub> </mrow> </semantics></math> of the USV.</p>
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<p>Framework of the DDPG algorithm.</p>
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<p>Amphibious USV propelled by single outboard motor for experimentation.</p>
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<p>Outboard engine parameters.</p>
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<p>Cumulative reward value curve for each episode.</p>
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<p>MATLAB path-following simulation model.</p>
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<p>Simulation experiment results of path following of a single straight path. (<b>a</b>) The comparison of the path-following trajectories. (<b>b</b>) The comparison of the cross error. (<b>c</b>) The comparison of the heading angle error.</p>
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<p>Simulation experiment results of path following of multi-polyline path. (<b>a</b>) Comparison of path-following trajectories. (<b>b</b>) Comparison of cross error. (<b>c</b>) Comparison of heading angle error.</p>
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<p>Path-following trajectories of real ship experiments. (<b>a</b>) Comparison of path-following trajectories. (<b>b</b>) Aerial view of path-following experiment.</p>
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<p>Comparison of path-following error in real ship experiment. (<b>a</b>) Comparison of cross error. (<b>b</b>) Comparison of heading angle error.</p>
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<p>Comparison of the three-degree-of-freedom speeds of the USV in real ship experiment. (<b>a</b>) Controlled by the DDPG-MPC algorithm. (<b>b</b>) Controlled by the ALOS-PID algorithm.</p>
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11 pages, 2330 KiB  
Article
Immunolocalization of Na(+)-Dependent Glucose Co-Transporters in Chicken Kidneys in Norm and During T-2 Mycotoxicosis (Primary Study)
by Cristin Allmang, Piret Hussar, Ilmārs Dūrītis and Florina Popovska-Percinic
Curr. Issues Mol. Biol. 2024, 46(12), 14259-14269; https://doi.org/10.3390/cimb46120854 - 18 Dec 2024
Viewed by 360
Abstract
The kidney plays an essential role in the proper homeostasis of glucose. In the kidney, glucose transport is carried out across cell membranes by two families of glucose transporters—facilitated diffusion glucose transporters (GLUTs) and Na(+)-dependent glucose co-transporters (SGLT family). Among the transporters, sodium-dependent [...] Read more.
The kidney plays an essential role in the proper homeostasis of glucose. In the kidney, glucose transport is carried out across cell membranes by two families of glucose transporters—facilitated diffusion glucose transporters (GLUTs) and Na(+)-dependent glucose co-transporters (SGLT family). Among the transporters, sodium-dependent glucose co-transporters play a major role in the kidney‘s ability to reabsorb glucose. Although the localization of glucose transporters has been extensively studied in mammals, there are still knowledge gaps regarding the localization of SGLTs in birds. The aim of this research was to conduct a comparative study of the immunolocalization of the sodium-dependent glucose co-transporters SGLT1 and SGLT2 in the kidneys of healthy and T-2-mycotoxicated chickens. Immunohistochemical staining was carried out using the polyclonal primary antibodies SGLT1 and SGLT2 (Abcam, UK) in kidney tissue derived from seven healthy and seven T-2-mycotoxicated 7-day-old female layer-type Ross chickens (Gallus gallus domesticus). The sections were stained using an immunohistochemistry kit (Abcam, UK). In the kidneys of the healthy birds, strong staining of SGLT1 and SGLT2 was observed in the cytoplasm of the epithelial cells of the proximal straight and convoluted tubules. In the kidneys of the birds of the T-2 toxin group, weak expression of SGLT1 and SGLT2 with morphological changes occurred, indicating reduced glucose transport in the urinary system during T-2 mycotoxicosis. Full article
(This article belongs to the Section Biochemistry, Molecular and Cellular Biology)
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<p>Na(+)-dependent glucose co-transporter 2 transmembrane transport in bird kidneys. SGLT2 = Na(+)-dependent glucose co-transporter 2; GLUT2 = facilitative glucose transport.</p>
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<p>Normal kidney morphology of a 7-day-old chicken: proximal (arrowheads) and distal tubules (arrows) in the cortex of the kidney. Hematoxylin and eosin. Magnification 400×, scale bar 100 µm.</p>
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<p>Immunolocalization of the sodium-dependent glucose co-transporter-1 (SGLT1) in kidney tissue (<b>a</b>) in healthy 7-day-old chickens; note the strong expression of SGLT1 in the apical part of the epithelial cells of renal proximal tubules (arrowheads). Magnification 400×, scale bar 50 µm; (<b>b</b>) damaged brush border membranes of proximal tubule’s epithelial cells in intoxicated chicken (arrows). Magnification 400×, scale bar 50 µm.</p>
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<p>Immunolocalization of sodium-dependent glucose co-transporter-2 (SGLT2) in (<b>a</b>) strongly stained proximal tubules (arrowheads) of healthy chicken kidney and weakly stained distal tubules (arrows) is observed. Magnification 400×, scale bar 50 µm; (<b>b</b>) the pale staining of proximal renal tubules (arrows) of intoxicated bird group is observed. Magnification 400×, scale bar 50 µm.</p>
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<p>SGLT2 in healthy 7-day-old chicken kidneys. Note the unstained collecting ducts (arrows); immunohistochemistry (IHC) magnification 400×, scale bar 50 µm.</p>
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10 pages, 1326 KiB  
Article
Pilot Study on the Relationship Between Different Lower Limb Raising Velocities and Trunk Muscle Contraction in Active Straight Leg Raise
by Kohei Yoshikawa, Noriyuki Kida, Takumi Jiroumaru, Yuta Murata and Shinichi Noguchi
J. Funct. Morphol. Kinesiol. 2024, 9(4), 276; https://doi.org/10.3390/jfmk9040276 - 18 Dec 2024
Viewed by 330
Abstract
Background/Objectives: The active straight leg raise requires intricate coordination between the hip, knee, pelvis, and spine. Despite its complexity, limited research has explored the relationship between lower limb raising velocity and trunk muscle motor control during an active straight leg raise in healthy [...] Read more.
Background/Objectives: The active straight leg raise requires intricate coordination between the hip, knee, pelvis, and spine. Despite its complexity, limited research has explored the relationship between lower limb raising velocity and trunk muscle motor control during an active straight leg raise in healthy individuals. This study aimed to explore the potential effects of increased lower limb raising velocity on core muscle contractions during active straight leg raises. Methods: Six healthy adult men (mean age: 24.5 ± 2.5 years) participated in this study. Electromyography signals were recorded using surface electrodes placed on the rectus abdominis, external oblique, and internal oblique/transverse abdominis muscles. The participants performed active straight leg raises at three different velocities: 3 s, 2 s, and as fast as possible (max). The electromyography data were analyzed from 250 ms before to 1000 ms after movement initiation, with muscle activity expressed as a percentage of the maximal voluntary isometric contraction. Statistical analyses were conducted using non-parametric tests, including the Friedman test for overall differences, followed by pairwise Wilcoxon signed-rank tests with Bonferroni correction for multiple comparisons (p < 0.05). Results: During the 250 ms before movement initiation, the internal oblique/transverse abdominis, external oblique, and rectus abdominis muscles showed greater activity in the max condition compared to the 3 s and 2 s conditions (Friedman test, p < 0.05), but no significant differences were found in pairwise comparisons (Wilcoxon test, p > 0.05). Similarly, during the 500 ms after movement initiation, internal oblique/transverse abdominis activity was higher in the max condition, with no significant pairwise differences observed. Conclusions: Faster lower limb raising velocities during active straight leg raise may enhance core stability by activating anticipatory and sustained internal oblique/transverse abdominis, external oblique, and rectus abdominis activity on the raised limb side. Training to promote this activation could improve dynamic stability in rapid or asymmetric movements. Full article
(This article belongs to the Section Functional Anatomy and Musculoskeletal System)
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<p>Experimental design of the active straight leg raise task.</p>
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9 pages, 205 KiB  
Article
Healthcare Access and County-Level COVID-19 Mortality: Exploring the Impact of Hospital Proximity and Uninsurance Rates
by Gabriel A. Benavidez and Anja Zgodic
Healthcare 2024, 12(24), 2543; https://doi.org/10.3390/healthcare12242543 - 17 Dec 2024
Viewed by 388
Abstract
Background/Objectives: Many social and environmental factors contribute to the disproportionate burden of COVID-19 mortality. Access to healthcare services has not been thoroughly examined as a factor contributing to COVID-19 mortality. This study examines distance to ERs and ICUs, uninsurance rates, and county-level COVID-19 [...] Read more.
Background/Objectives: Many social and environmental factors contribute to the disproportionate burden of COVID-19 mortality. Access to healthcare services has not been thoroughly examined as a factor contributing to COVID-19 mortality. This study examines distance to ERs and ICUs, uninsurance rates, and county-level COVID-19 mortality rates. Methods: Using data from the American Hospital Association survey, we identified hospitals providing emergency and intensive care services. Hospital locations were geocoded, and straight-line distance was calculated from the population-weighted county centroid. The county proportion of uninsured residents came from the American Community Survey. Generalized linear regression models with a log-link were used to examine study factors and county COVID-19 mortality rates. Results: A total of 2640 (84.0%) U.S. counties or county-equivalents were included in this analysis. The median COVID-19 mortality rate was 240 deaths per 100,000. In adjusted models, increasing distance to ERs (IRR: 0.95; 95% CI: 0.92, 0.98) or ICUs (IRR: 0.61; 95% CI: 0.57, 0.65) was not significantly associated with increased COVID-19 mortality. The proportion of residents (IRR: 3.81; CI: 2.58, 5.62) uninsured was significantly associated with increased COVID-19 mortality rates. Conclusions: Being in close proximity to hospital-based healthcare services may not provide any significant benefit for COVID-19 mortality outcomes, considering that hospitals are largely located in more densely populated areas conducive to COVID-19 spread. Financial barriers may largely contribute to persons avoiding necessary COVID-19 care. To continue to combat COVID-19 and future pandemics, greater attention should be focused on eliminating financial barriers to receiving medically necessary care. Full article
24 pages, 10520 KiB  
Article
A Hybrid Harmonic Curve Model for Multi-Streamer Hydrophone Positioning in Seismic Exploration
by Kaiwei Sang, Cuilin Kuang, Lingsheng Lv, Heng Liu, Haonan Zhang, Yijun Yang and Baocai Yang
Sensors 2024, 24(24), 8025; https://doi.org/10.3390/s24248025 - 16 Dec 2024
Viewed by 332
Abstract
Towed streamer positioning is a vital and essential stage in marine seismic exploration, and accurate hydrophone coordinates exert a direct and significant influence on the quality and reliability of seismic imaging. Current methods predominantly rely on analytical polynomial models for towed streamer positioning; [...] Read more.
Towed streamer positioning is a vital and essential stage in marine seismic exploration, and accurate hydrophone coordinates exert a direct and significant influence on the quality and reliability of seismic imaging. Current methods predominantly rely on analytical polynomial models for towed streamer positioning; however, these models often produce significant errors when fitting to streamers with high curvature, particularly during turning scenarios. To address this limitation, this study introduces a novel multi-streamer analytical positioning method that uses a hybrid harmonic function to model the three-dimensional coordinates of streamers. This approach mitigates the substantial modeling errors associated with polynomial models in high-curvature conditions and better captures the dynamic characteristics of streamer fluctuations. Firstly, the mathematical model for the hybrid harmonic function is constructed. Then, the algorithmic implementation of the model is detailed, along with the derivation of the error equation and the multi-sensor fusion solution process. Finally, the validity of the model is verified using both simulated and field data. The results demonstrate that, in the turning scenario without added error, the proposed harmonic model improves simulation accuracy by 35.5% compared to the analytical polynomial model, and by 27.2% when error is introduced. For field data, accuracy improves by 18.1%, underscoring the model’s effectiveness in significantly reducing errors associated with polynomial models in turning scenarios. The performance of the harmonic function model is generally comparable to that of the polynomial model in straight scenarios. Full article
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<p>Towed streamer exploration and positioning network.</p>
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<p>Hybrid harmonic function positioning model.</p>
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<p>Simulated positioning network configuration.</p>
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<p>Simulated data trajectory.</p>
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<p>Mean positioning deviation over epoch.</p>
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<p>Mean positioning deviation along offset in turning scenario.</p>
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<p>Mean positioning deviation along offset in straight scenario.</p>
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<p>Streamer shape in (<b>a</b>) 3790 s turning and (<b>b</b>) 8000 s straight scenario.</p>
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<p>Mean positioning deviation over epoch.</p>
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<p>Mean positioning deviation along offset in the turning scenario.</p>
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<p>Mean positioning deviation along offset in the straight scenario.</p>
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<p>Streamer shape in (<b>a</b>) 3790 s turning and (<b>b</b>) 8000 s straight scenario.</p>
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<p>Deviation quartile over (<b>a</b>) temporal and (<b>b</b>) spatial in turning scenario.</p>
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<p>Deviation quartile over (<b>a</b>) temporal and (<b>b</b>) spatial in straight scenario.</p>
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<p>Turning trajectory for field data.</p>
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<p>Mean positioning deviation over epoch.</p>
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<p>Mean positioning deviation along offset in the turning scenario.</p>
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<p>Streamer shape in (<b>a</b>) 10,000 s turning and (<b>b</b>) 5829.2 s straight scenario.</p>
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<p>Deviation quartile over temporal and spatial in turning (<b>a</b>,<b>b</b>) and straight (<b>c</b>,<b>d</b>) scenarios.</p>
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<p>Mean positioning deviation over epoch.</p>
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<p>Mean positioning deviation along offset in the straight scenario.</p>
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16 pages, 3072 KiB  
Article
Rock-Breaking Mechanism and Application of Combined Long and Short Holes in Parallel Holes Cut in Small-Section Tunnels
by Hongxian Fu and Yufan Gao
Appl. Sci. 2024, 14(24), 11626; https://doi.org/10.3390/app142411626 - 12 Dec 2024
Viewed by 445
Abstract
In order to address the issue of limited excavation footage in the drilling and blasting of a water diversion tunnel with a cross-section of approximately 10 m2, which is unable to meet the demands of rapid construction, a blasting method combining [...] Read more.
In order to address the issue of limited excavation footage in the drilling and blasting of a water diversion tunnel with a cross-section of approximately 10 m2, which is unable to meet the demands of rapid construction, a blasting method combining long and short straight-hole cutting was proposed based on the theories of elastic mechanics, blasting craters, explosive gas and stress waves. A mechanical model was established to elucidate the parameter design method and cavity formation principle of the combined cutting. Numerical simulation and field tests were employed to analyze the rock-breaking process of combined cutting, with a view to comparing the blasting effect differences between the traditional inclined cutting method and the combined cutting method. The research results indicate that during the blasting process with combined long and short straight-hole cutting, the uncharged portion of the deep hole can serve as an empty hole during the subsequent blasting of the shallow hole. The concentration of stress at the wall of the empty hole and the superposition of reflected and incident waves serve to enhance the rock-breaking effect of the shallow hole, with the enhancement being influenced by the diameter of the hole and the distance between it and the empty hole. The preferential detonation of the shallow hole can provide a smaller resistance line and free surface distance for deep hole detonation, creating favorable conditions for rock fragmentation in deep hole blasting, making it easier for the rock in the cutting area to be thrown out and increasing the utilization rate of the blast holes. The shape of the formed cavity is a long strip-shaped cube, with its volume being influenced by the spacing between each group of deep and shallow holes. The rock mass damage is most severe in the vertical direction, while the rock mass damage at the center of the upper and lower edges is relatively weaker. In order to optimize the utilization of blasting energy, it is essential to select an appropriate spacing between each group of blast holes. In comparison to the utilization of traditional inclined cuts, the implementation of combined long and short holes has been observed to result in a greater extent of blasting footage and relatively lower explosive consumption. These research findings provide a reference point for the rapid and efficient construction of small-section tunnel engineering, as well as the design of straight-hole cut blasting with reduced consumption. Full article
(This article belongs to the Special Issue New Challenges in Urban Underground Engineering)
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<p>Schematic diagram of long and short eye combination cutting groove: (<b>a</b>) hole layout; (<b>b</b>) charge placement in profile.</p>
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<p>Model structure and grid division.</p>
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<p>Effective stress cloud map of shallow hole blasting at different times: (<b>a</b>) t = 70 ms; (<b>b</b>) t = 110 ms; (<b>c</b>) t = 150 ms; (<b>d</b>) t = 200 ms.</p>
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<p>Effective stress cloud map of deep hole blasting at different times: (<b>a</b>) t = 270 ms; (<b>b</b>) t = 310 ms; (<b>c</b>) t = 370 ms; (<b>d</b>) t = 450 ms.</p>
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<p>Cloud map of shallow hole blasting damage at different times: (<b>a</b>) t = 110 ms; (<b>b</b>) t = 170 ms; (<b>c</b>) t = 200 ms; (<b>d</b>) t = 240 ms.</p>
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<p>Cloud map of deep hole blasting damage at different times: (<b>a</b>) t = 370 ms; (<b>c</b>) t = 460 ms; (<b>d</b>) t = 530 ms; (<b>b</b>) t = 1000 ms.</p>
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<p>Layout of boreholes for three types of blasting tests (unit: cm): (<b>a</b>) combined long and short hole cutting; (<b>b</b>) oblique cutting test 1; (<b>c</b>) oblique cutting test 2.</p>
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<p>The formation of the groove cavity after cut blasting: (<b>a</b>) drilling of cutting holes; (<b>b</b>) effect of cutting.</p>
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<p>The full-section blasting effect of the combined long and short holes: (<b>a</b>) blasting effect; (<b>b</b>) length of hole mark.</p>
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16 pages, 25986 KiB  
Article
Deformation Properties of Thermally Aged E308L Stainless Steel During Tensile Test with Carbide Effects
by Yongming Han, Xinyuan Cao, Yonghao Lu and Tetsuo Shoji
Materials 2024, 17(24), 6070; https://doi.org/10.3390/ma17246070 - 12 Dec 2024
Viewed by 313
Abstract
Microstructure and deformation properties of both unaged and aged cladding material were studied at 400 °C for 10,000 h. The results indicated that carbide formation occurred in the cladding material, while thermal aging treatment resulted in spinodal decomposition and G-phase formation in the [...] Read more.
Microstructure and deformation properties of both unaged and aged cladding material were studied at 400 °C for 10,000 h. The results indicated that carbide formation occurred in the cladding material, while thermal aging treatment resulted in spinodal decomposition and G-phase formation in the aged ferrite phase. Furthermore, intensive straight slip bands formed in both unaged and aged austenite phases. Continual straight slip bands formed in the unaged ferrite phase, while curvilinear slip bands formed in the aged ferrite phase during the plastic deformation process. Microcracks preferred to nucleate at the points of interaction between phase boundaries and carbides, while the aged ferrite phase experienced lowered microcrack formation along the carbide/ferrite phase boundary. Microcracks propagated along the straight slip bands in the unaged ferrite phases and curvilinear slip bands in the aged ferrite phases. Full article
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<p>(<b>a</b>) Microscope morphology of tensile test device and (<b>b</b>) schematic diagram of tensile sample.</p>
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<p>BSE images of the samples aged at 400 °C for (<b>a</b>) 0 h and (<b>b</b>) 10,000 h; (<b>c</b>) and (<b>d</b>) the corresponding magnified images of the black framed regions indicated in (<b>a</b>) and (<b>b</b>), respectively.</p>
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<p>(<b>a</b>) TEM image of the unaged cladding material, the corresponding SEAD pattern of austenite and carbide is shown in the inset, and (<b>b</b>) HRTEM image of the ferrite phase, the corresponding FFT image of ferrite is shown in the inset.</p>
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<p>(<b>a</b>) and (<b>c</b>) TEM image of the cladding material aged at 400 °C for 10,000 h, (<b>b</b>) SEAD pattern of ferrite phase and G-phase, (<b>c</b>) and (<b>d</b>) HRTEM images of spinodal decomposition and G-phase in the aged ferrite phase, respectively.</p>
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<p>BSE images of the unaged sample with (<b>a</b>) 0%, (<b>b</b>) 5.4%, (<b>c</b>) 10.2%, and (<b>d</b>) 12.8% elongation, (<b>e</b>) and (<b>f</b>) the magnified BSE and SEM images of the red framed region indicated in (<b>d</b>), respectively.</p>
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<p>(<b>a</b>,<b>c</b>,<b>e</b>) SEM and (<b>b</b>,<b>d</b>,<b>f</b>) corresponding BSE images of the unaged sample with 12.8% elongation.</p>
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<p>(<b>a</b>,<b>c</b>,<b>e</b>) SEM and (<b>b</b>,<b>d</b>,<b>f</b>) corresponding BSE images of the unaged sample with 12.8% elongation.</p>
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<p>SEM image of the aged sample with (<b>a</b>) 0%, (<b>b</b>) 5.4%, (<b>c</b>) 10.2%, and (<b>d</b>) 12.8% deformation elongation, (<b>e</b>,<b>f</b>) the magnified BSE and SEM images of the black framed region indicated in (<b>d</b>).</p>
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<p>SEM image of the aged sample with (<b>a</b>) 0%, (<b>b</b>) 5.4%, (<b>c</b>) 10.2%, and (<b>d</b>) 12.8% deformation elongation, (<b>e</b>,<b>f</b>) the magnified BSE and SEM images of the black framed region indicated in (<b>d</b>).</p>
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<p>(<b>a</b>) SEM and (<b>c</b>) BSE images of the aged ferrite phase at 12.8% elongation with no carbide formation along the phase boundary, (<b>b</b>) and (<b>d</b>) the corresponding magnified images of the aged ferrite phase, respectively.</p>
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<p>(<b>a</b>) SEM and (<b>c</b>) BSE images of the aged ferrite phase at 12.8% elongation with no carbide formation along the phase boundary, (<b>b</b>) and (<b>d</b>) the corresponding magnified images of the aged ferrite phase, respectively.</p>
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<p>(<b>a</b>) SEM and (<b>b</b>) BSE images of the aged ferrite phase at 12.8% elongation with carbide formation along the phase boundary, (<b>c</b>) and (<b>d</b>) the corresponding magnified images of the aged ferrite phase respectively.</p>
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<p>Overall appearance of the fractured samples aged at 400 °C for (<b>a</b>) 0 h and (<b>b</b>) 10,000 h, (<b>c</b>) and (<b>d</b>) the corresponding magnified images of the white framed regions indicated in (<b>a</b>) and (<b>b</b>), respectively.</p>
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<p>(<b>a</b>) TEM image of slip bands formed in the unaged austenite phase with 12.8% elongation, (<b>b</b>) TEM observation of unaged ferrite phase with 12.8% elongation, (<b>c</b>) HRTEM image of unaged ferrite phase, (<b>d</b>) the FFT image of (<b>c</b>), and (<b>e</b>) FFT image of (<b>d</b>).</p>
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<p>(<b>a</b>) TEM image of slip bands formed in the unaged austenite phase with 12.8% elongation, (<b>b</b>) TEM observation of unaged ferrite phase with 12.8% elongation, (<b>c</b>) HRTEM image of unaged ferrite phase, (<b>d</b>) the FFT image of (<b>c</b>), and (<b>e</b>) FFT image of (<b>d</b>).</p>
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<p>(<b>a</b>) TEM bright-field image of the aged cladding material, (<b>b</b>) HRTEM image of the aged ferrite phase, (<b>c</b>) and (<b>d</b>) the corresponding white and black framed regions indicated in (<b>b</b>), respectively, and (<b>e</b>) and (<b>f</b>) IFFT images of (<b>c</b>) and (<b>d</b>), respectively.</p>
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<p>(<b>a</b>) TEM bright-field image of the aged cladding material, (<b>b</b>) HRTEM image of the aged ferrite phase, (<b>c</b>) and (<b>d</b>) the corresponding white and black framed regions indicated in (<b>b</b>), respectively, and (<b>e</b>) and (<b>f</b>) IFFT images of (<b>c</b>) and (<b>d</b>), respectively.</p>
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<p>TEM images of (<b>a</b>) unaged ferrite phase and (<b>b</b>) aged ferrite phase.</p>
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<p>Schematic image of deformation behavior in the unaged and aged ferrite phase.</p>
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