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Metals, Volume 10, Issue 10 (October 2020) – 127 articles

Cover Story (view full-size image): An effective and feasible computational material design requires predictive material modeling supported by crucial experiments and validations. The key feature of this work is a combined experimental analysis and 2/3-dimensional phase-field simulation study, focusing on the solidification and precipitation nature of a hypoeutectic Al alloy. Demonstrating reliable modeling techniques and experimental cross-validation on the fundamental investigation of Al alloys can be expanded to various alloys, leading to an advanced mode of new material design. In this strategy, semiquantitative modeling of microstructural evolution during solidification was validated by experimental investigations. The cover image shows the simulated phase map and elemental distributions. View this paper.
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16 pages, 1513 KiB  
Review
Interfacial Aspects of Metal Matrix Composites Prepared from Liquid Metals and Aqueous Solutions: A Review
by Peter Baumli
Metals 2020, 10(10), 1400; https://doi.org/10.3390/met10101400 - 21 Oct 2020
Cited by 12 | Viewed by 3514
Abstract
The paper reviews the preparation of the different metallic nanocomposites. In the preparation of composites, especially in the case of nanocomposites, interfacial phenomena play an important role. This review summarizes the literature on various interfacial phenomena, such as wettability and reactivity in the [...] Read more.
The paper reviews the preparation of the different metallic nanocomposites. In the preparation of composites, especially in the case of nanocomposites, interfacial phenomena play an important role. This review summarizes the literature on various interfacial phenomena, such as wettability and reactivity in the case of casting techniques and colloidal behavior in the case of electrochemical and electroless methods. The main contribution of this work lies in the evaluation of collected interfacial phenomena and difficulties in the production of metal matrix composites, for both nano-sized and micro-sized reinforcements. This study can guide the composite maker in choosing the best criteria for producing metal matrix composites, which means a real interface with good adhesion between the matrix and the reinforcement. This criterion results in desirable mechanical and physical properties and homogenous dispersion of the reinforcement in the matrix. Full article
(This article belongs to the Special Issue Metallic Nanocomposites)
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<p>Methods and interfacial phenomena of metal matrix composite preparation.</p>
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<p>Interpretation of contact angle: (<b>a</b>) non-wetting; (<b>b</b>) wetting; (<b>c</b>) in case of perfect wetting.</p>
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<p>The reinforcement (C-fiber) and the matrix (aluminum) position in the case of a “non-wetting” and a “perfect wetting” system.</p>
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14 pages, 3894 KiB  
Article
Formation Mechanism of Micro- and Nanocrystalline Surface Layers in Titanium and Aluminum Alloys in Electron Beam Irradiation
by Sergei Nevskii, Vladimir Sarychev, Sergey Konovalov, Alexey Granovskii and Victor Gromov
Metals 2020, 10(10), 1399; https://doi.org/10.3390/met10101399 - 21 Oct 2020
Cited by 17 | Viewed by 2269
Abstract
The reported study discusses the formation of micro- and nanocrystalline surface layers in alloys on the example of Ti-Y and Al-Si-Y systems irradiated by electron beams. The study has established a crystallization mechanism of molten layers in the micro-and nanodimensional range, which involves [...] Read more.
The reported study discusses the formation of micro- and nanocrystalline surface layers in alloys on the example of Ti-Y and Al-Si-Y systems irradiated by electron beams. The study has established a crystallization mechanism of molten layers in the micro-and nanodimensional range, which involves a variety of hydrodynamic instabilities developing on the plasma–melt interface. As suggested, micro- and nanostructures form due to the combination of thermocapillary, concentration and capillary, evaporation and capillary and thermoelectric instabilities. This mechanism has provided the foundation for a mathematical model to describe the development of structures in focus in the electron beam irradiation. The study has pointed out that thermoelectric field strength E ≥ 106 V/m is attributed to the occurring combination of instabilities in micro- and nanodimensional ranges. A full dispersion equation of perturbations on the melt surface was analyzed. Full article
(This article belongs to the Special Issue Electron Beam Treatment Technology in Metals)
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<p>The structure of yttrium-doped titanium (<b>a</b>,<b>b</b>), and silumin (<b>c</b>,<b>d</b>) surfaces irradiated by an electron beam.</p>
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<p>Scheme of combination instability formation.</p>
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<p>A growth rate characteristic of perturbations on the plasma–titanium melt interface found when solving the Equation (11): (<b>1</b>) ignoring thermoelectric and evaporation and capillary effects, (<b>2</b>) including the thermoelectric effect only, (<b>3</b>) with regard to thermal and evaporation and capillary instabilities, (<b>4</b>) involving thermal, evaporation and capillarity instabilities and the thermoelectric effect.</p>
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<p>A growth rate characteristic of perturbations on the plasma–silumin melt interface found when solving the Equation (11): (<b>1</b>) ignoring thermoelectric and evaporation and capillary effects, (<b>2</b>) including the thermoelectric effect only, (<b>3</b>) with regard to thermal and evaporation and capillary instabilities, (<b>4</b>) involving thermal, evaporation and capillarity instabilities and the thermoelectric effect.</p>
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<p>A growth rate characteristic of perturbations on the plasma–melt interface for a thermoelectric constant of 10<sup>−1</sup> V/K: (<b>1</b>) Ti-Y system; (<b>2</b>) Al-Si-Y system.</p>
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<p>A growth rate characteristic of perturbations on the plasma–titanium melt interface for a gradient of surface concentration of 10 m<sup>−2</sup>/m found when solving the Equation (11): (<b>1</b>) ignoring thermoelectric and evaporation and capillary effects, (<b>2</b>) including the thermoelectric effect only, (<b>3</b>) with regard to thermal and evaporation and capillary instabilities, (<b>4</b>) involving thermal, evaporation and capillarity instabilities and the thermoelectric effect.</p>
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<p>A growth rate characteristic of perturbations on the plasma–silumin melt interface for a gradient of surface concentration of 10 m<sup>−2</sup>/m found when solving the Equation (11): (<b>1</b>) ignoring thermoelectric and evaporation and capillary effects, (<b>2</b>) including the thermoelectric effect only, (<b>3</b>) with regard to thermal and evaporation and capillary instabilities, (<b>4</b>) involving thermal, evaporation and capillarity instabilities and the thermoelectric effect.</p>
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<p>A growth rate characteristic of perturbations on the plasma–melt interface for the Ti-Y system found when solving the Equation (9): (<b>a</b>) ignoring thermoelectric and evaporation and capillary effects, (<b>b</b>) for thermoelectric field strength of 10<sup>5</sup> V/m, (<b>c</b>) for thermoelectric field strength of 10<sup>6</sup> V/m.</p>
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<p>A growth rate characteristic of perturbations on the plasma–melt interface for the Al-Si-Y system found when solving the Equation (9): (<b>a</b>) ignoring thermoelectric and evaporation and capillary effects, (<b>b</b>) for thermoelectric field strength of 10<sup>5</sup> V/m, (<b>c</b>) for thermoelectric field strength of 10<sup>6</sup> V/m.</p>
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9 pages, 1583 KiB  
Article
Morphology and Optical Properties of Thin Cd3As2 Films of a Dirac Semimetal Compound
by Natalia Kovaleva, Ladislav Fekete, Dagmar Chvostova and Andrei Muratov
Metals 2020, 10(10), 1398; https://doi.org/10.3390/met10101398 - 21 Oct 2020
Cited by 5 | Viewed by 2344
Abstract
Using atomic-force microscopy (AFM) and wide-band (0.02–8.5 eV) spectroscopic ellipsometry techniques, we investigated the morphology and optical properties of Cd3As2 films grown by non-reactive RF magnetron sputtering on two types of oriented crystalline substrates (100)p-Si and (001) α [...] Read more.
Using atomic-force microscopy (AFM) and wide-band (0.02–8.5 eV) spectroscopic ellipsometry techniques, we investigated the morphology and optical properties of Cd3As2 films grown by non-reactive RF magnetron sputtering on two types of oriented crystalline substrates (100)p-Si and (001) α-Al2O3. The AFM study revealed the grainy morphology of the films due to island incorporation during the film growth. The complex dielectric function spectra of the annealed Cd3As2/Al2O3 films manifest pronounced interband optical transitions at 1.2 and 3.0 eV, in excellent agreement with the theoretical calculations for the body centered tetragonal Cd3As2 crystal structure. We discovered that due to electronic excitations to the Cd(s) conical bands, the low-energy absorption edge of the annealed Cd3As2 films reveals a linear dependence. We found that for the annealed Cd3As2 films, the Cd(s) conical node may be shifted in energy by about 0.08–0.18 eV above the heavy-flat As(p) valence band, determining the optical gap value. The as-grown Cd3As2 films exhibit the pronounced changes of the electronic band structure due to the doping effect associated with Cd non-stoichiometry, where fine-tuning of the Cd concentration may result in the gapless electronic band structure of Dirac semimetals. Full article
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<p>Typical AFM images of the surface morphology of the Cd<math display="inline"><semantics> <msub> <mrow/> <mn>3</mn> </msub> </semantics></math>As<math display="inline"><semantics> <msub> <mrow/> <mn>2</mn> </msub> </semantics></math> films grown by non-reactive RF magnetron sputtering on the polished oriented single-crystalline wafers (<b>a</b>) (100)<span class="html-italic">p</span>-Si and (<b>b</b>) (001) <math display="inline"><semantics> <mi>α</mi> </semantics></math>-Al<math display="inline"><semantics> <msub> <mrow/> <mn>2</mn> </msub> </semantics></math>O<math display="inline"><semantics> <msub> <mrow/> <mn>3</mn> </msub> </semantics></math>. The scan size is 1 × 1 <math display="inline"><semantics> <mi mathvariant="sans-serif">μ</mi> </semantics></math>m<math display="inline"><semantics> <msup> <mrow/> <mn>2</mn> </msup> </semantics></math>.</p>
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<p>(<b>a</b>,<b>c</b>) The imaginary parts of the dielectric function <math display="inline"><semantics> <mrow> <msub> <mi>ε</mi> <mn>2</mn> </msub> <mrow> <mo>(</mo> <mi>ω</mi> <mo>)</mo> </mrow> </mrow> </semantics></math> and refractive index <span class="html-italic">k</span> and (<b>b</b>,<b>d</b>) the real parts of the dielectric function <math display="inline"><semantics> <mrow> <msub> <mi>ε</mi> <mn>1</mn> </msub> <mrow> <mo>(</mo> <mi>ω</mi> <mo>)</mo> </mrow> </mrow> </semantics></math> and refractive index <span class="html-italic">n</span> for the annealed Cd<math display="inline"><semantics> <msub> <mrow/> <mn>3</mn> </msub> </semantics></math>As<math display="inline"><semantics> <msub> <mrow/> <mn>2</mn> </msub> </semantics></math>/Si (sample 908, 10 W, 80 min, 20 min annealing at 520 K) and Cd<math display="inline"><semantics> <msub> <mrow/> <mn>3</mn> </msub> </semantics></math>As<math display="inline"><semantics> <msub> <mrow/> <mn>2</mn> </msub> </semantics></math>/Al<math display="inline"><semantics> <msub> <mrow/> <mn>2</mn> </msub> </semantics></math>O<math display="inline"><semantics> <msub> <mrow/> <mn>3</mn> </msub> </semantics></math> (sample 909, 10 W, 40 min, 20 min annealing at 520 K) films, shown by solid blue and green curves, respectively. The thickness estimated from the model simulations was 91 ± 5 nm for the Cd<math display="inline"><semantics> <msub> <mrow/> <mn>3</mn> </msub> </semantics></math>As<math display="inline"><semantics> <msub> <mrow/> <mn>2</mn> </msub> </semantics></math>/Si film and 46 ± 3 nm for the Cd<math display="inline"><semantics> <msub> <mrow/> <mn>3</mn> </msub> </semantics></math>As<math display="inline"><semantics> <msub> <mrow/> <mn>2</mn> </msub> </semantics></math>/Al<math display="inline"><semantics> <msub> <mrow/> <mn>2</mn> </msub> </semantics></math>O<math display="inline"><semantics> <msub> <mrow/> <mn>3</mn> </msub> </semantics></math> film.</p>
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<p>The respective optical conductivity spectra, <math display="inline"><semantics> <mrow> <msub> <mi>σ</mi> <mn>1</mn> </msub> <mrow> <mo>(</mo> <mi>ω</mi> <mo>)</mo> </mrow> <mo>=</mo> <mfrac> <mn>1</mn> <mrow> <mn>4</mn> <mi>π</mi> </mrow> </mfrac> <mi>ω</mi> <msub> <mi>ε</mi> <mn>2</mn> </msub> <mrow> <mo>(</mo> <mi>ω</mi> <mo>)</mo> </mrow> </mrow> </semantics></math>, for the annealed Cd<math display="inline"><semantics> <msub> <mrow/> <mn>3</mn> </msub> </semantics></math>As<math display="inline"><semantics> <msub> <mrow/> <mn>2</mn> </msub> </semantics></math> films.</p>
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<p>The absorption spectra <math display="inline"><semantics> <mrow> <mi>α</mi> <mo>(</mo> <mi>ω</mi> <mo>)</mo> </mrow> </semantics></math> for the annealed Cd<math display="inline"><semantics> <msub> <mrow/> <mn>3</mn> </msub> </semantics></math>As<math display="inline"><semantics> <msub> <mrow/> <mn>2</mn> </msub> </semantics></math>/Si and Cd<math display="inline"><semantics> <msub> <mrow/> <mn>3</mn> </msub> </semantics></math>As<math display="inline"><semantics> <msub> <mrow/> <mn>2</mn> </msub> </semantics></math>/Al<math display="inline"><semantics> <msub> <mrow/> <mn>2</mn> </msub> </semantics></math>O<math display="inline"><semantics> <msub> <mrow/> <mn>3</mn> </msub> </semantics></math> films shown for (<b>a</b>) the wide spectral range and (<b>b</b>) at the low-energy edge (shown by solid blue and green curves and symbols, respectively). The gray solid lines show linear extrapolations (<math display="inline"><semantics> <mrow> <mi>y</mi> <mo>=</mo> <mi>a</mi> <mo>+</mo> <mi>b</mi> <mi>x</mi> </mrow> </semantics></math>) of the low-energy absorption edge (for Cd<math display="inline"><semantics> <msub> <mrow/> <mn>3</mn> </msub> </semantics></math>As<math display="inline"><semantics> <msub> <mrow/> <mn>2</mn> </msub> </semantics></math>/Si: <math display="inline"><semantics> <mrow> <mi>a</mi> <mo>=</mo> <mo>−</mo> <mn>0.017</mn> <mo>±</mo> <mn>2</mn> <mo>%</mo> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <mi>b</mi> <mo>=</mo> <mn>0.093</mn> <mo>±</mo> <mn>2</mn> <mo>%</mo> </mrow> </semantics></math> and for Cd<math display="inline"><semantics> <msub> <mrow/> <mn>3</mn> </msub> </semantics></math>As<math display="inline"><semantics> <msub> <mrow/> <mn>2</mn> </msub> </semantics></math>/Al<math display="inline"><semantics> <msub> <mrow/> <mn>2</mn> </msub> </semantics></math>O<math display="inline"><semantics> <msub> <mrow/> <mn>3</mn> </msub> </semantics></math>: <math display="inline"><semantics> <mrow> <mi>a</mi> <mo>=</mo> <mo>−</mo> <mn>0.005</mn> <mo>±</mo> <mn>9</mn> <mo>%</mo> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <mi>b</mi> <mo>=</mo> <mn>0.065</mn> <mo>±</mo> <mn>4</mn> <mo>%</mo> </mrow> </semantics></math>).</p>
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<p>(<b>a</b>,<b>b</b>) The imaginary <math display="inline"><semantics> <mrow> <msub> <mi>ε</mi> <mn>2</mn> </msub> <mrow> <mo>(</mo> <mi>ω</mi> <mo>)</mo> </mrow> </mrow> </semantics></math> and real <math display="inline"><semantics> <mrow> <msub> <mi>ε</mi> <mn>1</mn> </msub> <mrow> <mo>(</mo> <mi>ω</mi> <mo>)</mo> </mrow> </mrow> </semantics></math> parts of the complex dielectric function of the as-grown Cd<math display="inline"><semantics> <msub> <mrow/> <mn>3</mn> </msub> </semantics></math>As<math display="inline"><semantics> <msub> <mrow/> <mn>2</mn> </msub> </semantics></math> films on the polished oriented single-crystalline wafers (100)<span class="html-italic">p</span>-Si. The dashed blue curve corresponds to the data shown by the solid blue line in <a href="#metals-10-01398-f002" class="html-fig">Figure 2</a>. The solid blue, cyan, and magenta curves correspond to the ellipsometry measurements for Samples 908 (annealed), 904 (as-grown, 10 W, 20 min), and 905 (as-grown, 10 W, 80 min), respectively, obtained using a J.A. Woollam VASE ellipsometer.</p>
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14 pages, 7513 KiB  
Article
Optimization of Open Die Ironing Process through Artificial Neural Network for Rapid Process Simulation
by Silvia Mancini, Luigi Langellotto, Giovanni Zangari, Riccardo Maccaglia and Andrea Di Schino
Metals 2020, 10(10), 1397; https://doi.org/10.3390/met10101397 - 21 Oct 2020
Cited by 2 | Viewed by 2852
Abstract
The open die forging sequence design and optimization are usually performed by simulating many different configurations corresponding to different forging strategies. Finite element analysis (FEM) is a tool able to simulate the open die forging process. However, FEM is relatively slow and therefore [...] Read more.
The open die forging sequence design and optimization are usually performed by simulating many different configurations corresponding to different forging strategies. Finite element analysis (FEM) is a tool able to simulate the open die forging process. However, FEM is relatively slow and therefore it is not suitable for the rapid design of online forging processes. A new approach is proposed in this work in order to describe the plastic strain at the core of the piece. FEM takes into account the plastic deformation at the core of the forged pieces. At the first stage, a thermomechanical FEM model was implemented in the MSC.Marc commercial code in order to simulate the open die forging process. Starting from the results obtained through FEM simulations, a set of equations describing the plastic strain at the core of the piece have been identified depending on forging parameters (such as length of the contact surface between tools and ingot, tool’s connection radius, and reduction of the piece height after the forging pass). An Artificial Neural Network (ANN) was trained and tested in order to correlate the equation coefficients with the forging to obtain the behavior of plastic strain at the core of the piece. Full article
(This article belongs to the Special Issue Mechanical Properties and Microstructure of Forged Steel)
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<p>Schematic representation of the simulated forging process.</p>
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<p>Effect of the presence of manipulator during forging process for a Sb<sub>0</sub> of 300 mm.</p>
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<p>Total equivalent plastic strain at the core of the piece for an ingot with a diameter of 300 mm, 25% reduction, for Sb0 of 300 mm and a ΔSb0 of 10% at T = 1200 °C for the first series of strokes.</p>
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<p>Schematic representation of forged piece simulated; results have been token at the core of the piece in terms of plastic strain as a function of the length.</p>
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<p>Evolution of plastic strain as a function of length at 1200 °C, Sb<sub>0</sub> = 300 mm, reduction = 25%, ingot diameter equal to 300 mm, pitch 90%.</p>
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<p>Plot of C1 from the analytical model C1 (target) versus the ANN trained C1 in blue with error bands at +5% and −5% in grey (<b>a</b>) and the analytical model C2 (target) versus the ANN trained C2 in blue with error bands at +5% and −5% in grey (<b>b</b>).</p>
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<p>Plot of D1 from the analytical model D1 (target) versus the ANN trained D1 in blue with error bands at +5% and −5% in grey (<b>a</b>) and the analytical model D2 (target) versus the ANN trained D2 in blue with error bands at +5% and −5% in grey (<b>b</b>).</p>
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<p>Plot of M from the analytical model M (target) versus the ANN trained M in blue with error bands at +5% and −5% in grey.</p>
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<p>Total equivalent plastic strain as a function of length for Sb<sub>0</sub> = 150 mm, reduction of 5%, first stroke at (<b>a</b>) 800 °C, (<b>b</b>) 1200 °C.</p>
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<p>Total equivalent plastic strain as a function of length for Sb<sub>0</sub> = 150 mm, reduction of 25%, first stroke at (<b>a</b>) 800 °C, (<b>b</b>) 1200 °C.</p>
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<p>42CrMo4. Flow stress curves by hot forming. <a href="#metals-10-01397-f005" class="html-fig">Figure 5</a>.309 in [<a href="#B44-metals-10-01397" class="html-bibr">44</a>].</p>
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<p>Total equivalent plastic strain as a function of length for Sb<sub>0</sub> = 300 mm, reduction of 25% for first stroke at (<b>a</b>) 800 °C, (<b>b</b>) 1200 °C.</p>
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<p>Total equivalent plastic strain as a function of length for Sb<sub>0</sub> = 750 mm, reduction of 25% for first stroke at (<b>a</b>) 800 °C, (<b>b</b>) 1200 °C.</p>
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<p>Total equivalent plastic strain as a function of length for Sb<sub>0</sub> = 300 mm, reduction of 25% at 1200 °C for second (<b>a</b>) and third stroke (<b>b</b>).</p>
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7 pages, 2775 KiB  
Article
Nanoporous High-Entropy Alloy by Liquid Metal Dealloying
by Artem Vladimirovich Okulov, Soo-Hyun Joo, Hyoung Seop Kim, Hidemi Kato and Ilya Vladimirovich Okulov
Metals 2020, 10(10), 1396; https://doi.org/10.3390/met10101396 - 21 Oct 2020
Cited by 33 | Viewed by 5002
Abstract
High-entropy nanomaterials possessing high accessible surface areas have demonstrated outstanding catalytic performance, beating that found for noble metals. In this communication, we report about the synthesis of a new, nanoporous, high-entropy alloy (HEA) possessing open porosity. The nanoporous, high-entropy Ta19.1Mo20.5 [...] Read more.
High-entropy nanomaterials possessing high accessible surface areas have demonstrated outstanding catalytic performance, beating that found for noble metals. In this communication, we report about the synthesis of a new, nanoporous, high-entropy alloy (HEA) possessing open porosity. The nanoporous, high-entropy Ta19.1Mo20.5Nb22.9V30Ni7.5 alloy (at%) was fabricated from a precursor (TaMoNbV)25Ni75 alloy (at%) by liquid metal dealloying using liquid magnesium (Mg). Directly after dealloying, the bicontinuous nanocomposite consisting of a Mg-rich phase and a phase with a bulk-centered cubic (bcc) structure was formed. The Mg-rich phase was removed with a 3M aqueous solution of nitric acid to obtain the open, porous, high-entropy Ta19.1Mo20.5Nb22.9V30Ni7.5 alloy (at%). The ligament size of this nanoporous HEA is about 69 ± 9 nm, indicating the high surface area in this material. Full article
(This article belongs to the Special Issue Nanoporous and Nanocomposite Materials by Dealloying)
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<p>Selection of elements for liquid metal dealloying. (<b>a</b>) The values of <math display="inline"><semantics> <mrow> <mo>Δ</mo> <msubsup> <mi>H</mi> <mrow> <mrow> <mo>(</mo> <mrow> <mi>A</mi> <mi>B</mi> </mrow> <mo>)</mo> </mrow> </mrow> <mrow> <mi>m</mi> <mi>i</mi> <mi>x</mi> </mrow> </msubsup> </mrow> </semantics></math> (kJ/mol) calculated by Miedema’s model for atomic pairs between Mg and elements indicated in the plot [<a href="#B46-metals-10-01396" class="html-bibr">46</a>]; (<b>b</b>) Required relationship of the values of enthalpy of mixing between elements for the liquid metal dealloying of a master alloy AB in a liquid metal C.</p>
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<p>Schematic illustration of liquid metal dealloying process.</p>
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<p>X-ray diffraction pattern and scanning electron micrograph of the nanoporous high-entropy TaMoNbVNi alloy.</p>
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<p>Ligament size versus homologous temperature in conventional nano- and microporous materials and the nanoporous high-entropy alloys (HEAs) [<a href="#B19-metals-10-01396" class="html-bibr">19</a>] (note: non-LMD represents the nanoporous materials obtained by chemical dealloying [<a href="#B49-metals-10-01396" class="html-bibr">49</a>]; the dealloying time is different from that for the LMD-based materials: 10 min—open symbols, 20 min—half-open symbols, and 60 min—closed symbols).</p>
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11 pages, 7292 KiB  
Article
Coupling Finite Element Analysis and the Theory of Critical Distances to Estimate Critical Loads in Al6060-T66 Tubular Beams Containing Notches
by Marcos Sánchez, Sergio Cicero, Borja Arroyo and José Alberto Álvarez
Metals 2020, 10(10), 1395; https://doi.org/10.3390/met10101395 - 20 Oct 2020
Cited by 8 | Viewed by 2099
Abstract
This paper validates a methodology for the estimation of critical loads in tubular beams containing notch-type defects. The methodology is particularized for the case of Al6060-T66 tubular cantilever beams containing U-shaped notches. It consists in obtaining the stress field at the notch tip [...] Read more.
This paper validates a methodology for the estimation of critical loads in tubular beams containing notch-type defects. The methodology is particularized for the case of Al6060-T66 tubular cantilever beams containing U-shaped notches. It consists in obtaining the stress field at the notch tip using finite element analysis (FEA) and the subsequent application of the theory of critical distances (TCD) to derive the corresponding critical load (or load-bearing capacity). The results demonstrate that this methodology provides satisfactory predictions of fracture loads. Full article
(This article belongs to the Special Issue Computational Methods for Fatigue and Fracture)
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<p>Tensile test specimens. Dimensions in mm.</p>
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<p>Schematic of fracture single edge notched bend (SENB) specimens. Dimensions in mm.</p>
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<p>Experimental setup.</p>
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<p>Schematic of the tubular cantilever beams containing a U-notch close to the fixed support.</p>
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<p>Geometry of the model used in finite element (FE) simulations, showing the middle line on the fracture section (<b>a</b>) and the generated mesh (<b>b</b>).</p>
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<p>Obtaining theory of critical distances (TCD) parameters using the stress–distance curves.</p>
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<p>(<b>a</b>) Mesh employed in the FEA (finite element analysis) of the tubular beams; (<b>b</b>) detail of the notch tip.</p>
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<p>Load–displacement curves of some of the fracture tests.</p>
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<p>Load–displacement curves of the different tubular beam.</p>
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<p>Stress–distance curves at critical load in SENB specimens. The solid circles correspond to the cutoff points.</p>
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<p>Stress–distance curves in tubular beams when applying a unit load (1 N) at the free end.</p>
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<p>Comparison between the experimental results (LBCexp) and the resulting estimations (LBCest).</p>
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21 pages, 5971 KiB  
Article
A Study on the Stability Fields of Arc Plasma in the HPSR Process
by Michael Andreas Zarl, Manuel Andreas Farkas and Johannes Schenk
Metals 2020, 10(10), 1394; https://doi.org/10.3390/met10101394 - 20 Oct 2020
Cited by 19 | Viewed by 2867
Abstract
One of the major challenges for Europe’s future steel production will be minimizing the inherent process emissions in the production of crude steel based on iron ores. In this case, mainly the reduction of CO2 emissions is a focus. One promising process [...] Read more.
One of the major challenges for Europe’s future steel production will be minimizing the inherent process emissions in the production of crude steel based on iron ores. In this case, mainly the reduction of CO2 emissions is a focus. One promising process to overcome these problems is the hydrogen plasma smelting reduction (HPSR) process. This process has been studied for several years already at the Chair of Ferrous Metallurgy at Montanuniversitaet Leoben. The work presented focused on the stability of plasma arcs in the DC transferred arc system of the HPSR process. The stable operating plasma arc is of utmost importance for the future development of the process. The major objective is the definition of the most favorable conditions for this kind of arc. Therefore, tests were conducted to define fields of a stable operating plasma arc for multiple gas compositions and process variables. For several gas compositions of argon, nitrogen, argon/nitrogen, argon/hydrogen and nitrogen/hydrogen, fields of stability were measured and defined. Besides, the major influencing parameters and trends for the fields of stability were evaluated and are shown in this work. Full article
(This article belongs to the Section Extractive Metallurgy)
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<p>Example of a field of stability for the DC transferred arc.</p>
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<p>Gas composition of an H<sub>2</sub>–Ar mixture over the temperature at 100 kPa (FactSage™ 7.1, Database; FactPS 2017) [14.]</p>
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<p>Schematic diagrams for the activation barriers for the different reduction of metal oxides by different hydrogen species [<a href="#B18-metals-10-01394" class="html-bibr">18</a>].</p>
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<p>Simulation of the temperature distribution in an argon plasma flame using a tungsten electrode, operating at 150 A for 20 s [<a href="#B19-metals-10-01394" class="html-bibr">19</a>].</p>
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<p>Schematic visualization of the effects of the arc shift between the hollow graphite electrode (HGE) and the steel bath on the thermal profile in hydrogen plasma smelting reduction (HPSR) processes.</p>
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<p>Some examples of the arc geometries in the air in a constant gap [<a href="#B20-metals-10-01394" class="html-bibr">20</a>].</p>
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<p>Example of the chaotic movement of the arc due to the increase in the arc current [<a href="#B20-metals-10-01394" class="html-bibr">20</a>].</p>
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<p>Schematic for the definition of the absolute and relative errors during the operation.</p>
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<p>Reactor layout and list of the most important components reproduced from Reference [<a href="#B15-metals-10-01394" class="html-bibr">15</a>] with permission.</p>
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<p>Hi-Doser 0.2l, powder-dosing instrument.</p>
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<p>The simple circuit diagram with the use of a silicon-controlled rectifier (SCR) and the positions of measurement for the HPSR lab facility.</p>
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<p>Camera system and a sketch of the mounting on the lid of the HPSR lab reactor.</p>
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<p>Measurement for the first series of trials in set 1. Pure argon 20 mm arc gap in the idle centered position.</p>
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<p>Different positions for the arc during operation: (<b>a</b>) stable centered position; (<b>b</b>) position at the operation limit; (<b>c</b>) invalid position and signs of instability; and (<b>d</b>) invalid position, and chaotic behavior.</p>
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<p>Example of the evaluation of the field of stability for 100% nitrogen.</p>
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<p>Arc stability fields for the variation of the gas composition and the effect of iron ore introduction via the HGE.</p>
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<p>Arc stability fields for the variation of the hydrogen content and the effect of iron ore introduction through the HGE.</p>
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8 pages, 3231 KiB  
Article
Hydrochloric Acid Leaching Behaviors of Copper and Antimony in Speiss Obtained from Top Submerged Lance Furnace
by Sujin Chae, Kyoungkeun Yoo, Carlito Baltazar Tabelin and Richard Diaz Alorro
Metals 2020, 10(10), 1393; https://doi.org/10.3390/met10101393 - 20 Oct 2020
Cited by 6 | Viewed by 4250
Abstract
Copper (Cu) has been recovered from speiss generated from top submerged lance furnace process, but it was reported that the leaching efficiency of Cu in sulfuric acid solution decreased with increasing antimony (Sb) content in the speiss. Scanning electron microscopy (SEM)–energy-dispersive X-ray spectroscopy [...] Read more.
Copper (Cu) has been recovered from speiss generated from top submerged lance furnace process, but it was reported that the leaching efficiency of Cu in sulfuric acid solution decreased with increasing antimony (Sb) content in the speiss. Scanning electron microscopy (SEM)–energy-dispersive X-ray spectroscopy (EDS) results indicate that Sb exists as CuSb alloy, which would retard the leaching of Cu. Therefore, hydrochloric acid leaching with aeration was performed to investigate the leaching behaviors of copper and antimony. The leaching efficiency of Cu increased with increasing agitation speed, temperature, HCl concentration, and the introduction ratio of O2, but also with decreasing pulp density. The leaching efficiency of Cu increased to more than 99% within 60 min in 1 mol/L HCl solution at 600 rpm and 90 °C with 10 g/L pulp density and 1000 cc/min O2. The leaching efficiency of Sb increased and then decreased in all 1 mol/L HCl leaching tests, and precipitate was observed in the leach solution, which was determined to be SbOCl or Sb2O3 by XRD analyses. However, in 2 mol/L–5 mol/L HCl solutions, the leaching efficiency of Sb increased to more than 95% (about 900 mg/L) and remained, so more than 2 mol/L HCl could stabilize Sb ion in the HCl solution. Full article
(This article belongs to the Special Issue Advances in Selective Flotation and Leaching Process in Metallurgy)
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<p>Schematic diagram of metal recovery process from speiss of top submerged lance process.</p>
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<p>SEM image of sulfuric acid leaching residue of the speiss.</p>
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<p>Leaching efficiencies of (<b>a</b>) Cu and (<b>b</b>) Sb with time in the function of agitation speed.</p>
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<p>XRD pattern of leaching residue obtained from HCl leaching test in <a href="#metals-10-01393-f003" class="html-fig">Figure 3</a>.</p>
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<p>Leaching efficiencies of (<b>a</b>) Cu and (<b>b</b>) Sb with time in the function of gas introduction rate.</p>
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<p>Leaching efficiencies of (<b>a</b>) Cu and (<b>b</b>) Sb with time in the function of HCl concentration.</p>
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<p>Leaching efficiencies of (<b>a</b>) Cu and (<b>b</b>) Sb with time as a function of temperature.</p>
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<p>Leaching efficiencies of (<b>a</b>) Cu and (<b>b</b>) Sb with time in the function of pulp density.</p>
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<p>XRD pattern of leaching residue obtained from HCl leaching test in <a href="#metals-10-01393-f008" class="html-fig">Figure 8</a>.</p>
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12 pages, 4880 KiB  
Article
Numerical Simulation and Experimental Investigation on Electron Beam Welding of Spray-Formed 7055 Aluminum Alloy
by Shaogang Wang, Zheng Wang, Chengcong Zhang and Zhiguo Wang
Metals 2020, 10(10), 1392; https://doi.org/10.3390/met10101392 - 20 Oct 2020
Cited by 3 | Viewed by 2568
Abstract
The spray-formed 7055 aluminum alloy is welded by electron beam welding. Combined with the numerical simulation of a welding temperature field, the effect of different welding procedures on the microstructure and mechanical properties of welded joints is investigated in this study. Results show [...] Read more.
The spray-formed 7055 aluminum alloy is welded by electron beam welding. Combined with the numerical simulation of a welding temperature field, the effect of different welding procedures on the microstructure and mechanical properties of welded joints is investigated in this study. Results show that the joints with good properties can be obtained under proper welding procedures. The microstructure analysis demonstrates that the fusion zone mainly consists of equiaxed grains, while a fine equiaxed grain zone is formed near the fusion line. There are mainly α(Al), MgZn2, Al2CuMg, and Mg32(Al,Zn)49 phases in the weld metal. The morphology of the weld can be improved by modification welding after the first bead welding, which is also advantageous to the mechanical properties of a welded joint. In the as-welded condition, compared with that of the base metal, the hardness of the weld zone decreased to a certain extent. The maximum tensile strength of a welded joint reaches 371.7 MPa. There are many dimples on the tensile fracture surface of a welded joint, and it dominantly presents the characteristic of ductile fracture. The simulated molten pool is consistent with the experimental weld morphology, and the reliability and accuracy of the simulation analysis are verified. Full article
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<p>Thermal properties of 7055 alloy.</p>
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<p>Appearance of weld: (<b>a</b>) joint 4 and (<b>b</b>) joint 5.</p>
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<p>Microstructure of the joint transition zone without modification welding: (<b>a</b>) low magnification, and (<b>b</b>) high magnification.</p>
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<p>Microstructure of joint transition zone with modification welding: (<b>a</b>) low magnification, (<b>b</b>) high magnification, and (<b>c</b>) the modification welding zone.</p>
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<p>X-ray diffraction pattern of weldment.</p>
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<p>Transmission electron microscope (TEM) images of weldment: (<b>a</b>) within the grain in the fusion zone (FZ), (<b>b</b>) grain boundary in the FZ, (<b>c</b>) near heat-affected zone (HAZ), and (<b>d</b>) far-HAZ.</p>
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<p>Microhardness distribution of welded joints: (<b>a</b>) perpendicular to the weld center and (<b>b</b>) parallel to the weld center.</p>
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<p>Tensile facture morphologies of welded joints: (<b>a</b>) joint 4, (<b>b</b>) joint 5, (<b>c</b>) magnification of yellow rectangle c in (<b>a</b>), (<b>d</b>) magnification of yellow rectangle d in (<b>b</b>), (<b>e</b>) magnification of red rectangle e in (<b>a</b>), and (<b>f</b>) magnification of red rectangle f in (<b>b</b>).</p>
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<p>Comparison between simulated molten pool and experimental weld morphology: (<b>a</b>) without modification welding and (<b>b</b>) with modification welding.</p>
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<p>Temperature field distribution of 7055 alloy joint by electron beam welding (EBW).</p>
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<p>Weld thermal cycle curves of points A and B.</p>
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12 pages, 6162 KiB  
Article
Evolution of the Fretting Wear Damage of a Complex Phase Compound Layer for a Nitrided High-Carbon High-Chromium Steel
by Yong Duan, Shengguan Qu, Siyu Jia and Xiaoqiang Li
Metals 2020, 10(10), 1391; https://doi.org/10.3390/met10101391 - 19 Oct 2020
Cited by 2 | Viewed by 2262
Abstract
In this paper, the X210CrW12 steel was subjected to gas nitriding to obtain a complex phase compound layer with limited porosity. The nitrided layer was characterized by scanning electron microscopy (SEM), energy dispersive spectroscopy (EDS) and X-ray diffraction (XRD). The fretting wear behavior [...] Read more.
In this paper, the X210CrW12 steel was subjected to gas nitriding to obtain a complex phase compound layer with limited porosity. The nitrided layer was characterized by scanning electron microscopy (SEM), energy dispersive spectroscopy (EDS) and X-ray diffraction (XRD). The fretting wear behavior and the evolution of fretting wear damage of the compound layer were studied, and the worn surfaces were characterized by SEM/EDS and 3D optical profilometry. The results indicated that the compound layer showed superior fretting wear resistance and sufficient load-carrying capacity in the low loading case of 35 N, but the fracture of coarse nitrides (transformed primary carbides) was obviously detrimental to wear resistance. For the high loading case of 70 N, the low toughness of the compound layer led to the occurrence of brittle cracks, and the decrease in the thickness of the compound layer due to wear resulted in the cracking and spalling of the compound layer. Full article
(This article belongs to the Special Issue Machinability and Tribological Performance of Advanced Alloys)
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<p>Schematic diagram of ball-on-disk fretting tribometer.</p>
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<p>Cross-sectional microstructure of the nitrided layer: (<b>a</b>) overall features, (<b>b</b>) a close view of the rectangle in (<b>a</b>) and (<b>c</b>) energy dispersive spectroscopy (EDS) analysis of the point in (<b>b</b>).</p>
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<p>Cross-sectional hardness–depth profile for the nitrided specimen.</p>
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<p>X-ray diffraction from the surface of (<b>a</b>) un-nitrided specimen, (<b>b</b>) nitrided specimen before polishing and (<b>c</b>) nitrided specimen after polishing.</p>
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<p>Evolution of friction coefficient under the load of (<b>a</b>) 35 N and (<b>b</b>) 70 N.</p>
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<p>Wear volume of the nitrided specimens under the load of 35 N and 70 N.</p>
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<p>3D surface morphologies, cross-sectional profiles and scanning electron microscopy using backscattered electron mode (SEM-BSE) images of the wear scars after fretting cycles of 24 × 10<sup>3</sup> (<b>a</b>–<b>d</b>), 48 × 10<sup>3</sup> (<b>e</b>–<b>h</b>) and 72 × 10<sup>3</sup> (<b>i</b>–<b>l</b>) under the normal load of 35 N.</p>
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<p>EDS analysis of the dark area (the point in <a href="#metals-10-01391-f007" class="html-fig">Figure 7</a>h).</p>
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<p>(<b>a</b>) Worn surface at the center of the wear scar after 72 × 10<sup>3</sup> cycles under the normal load of 35 N. (<b>b</b>) Higher magnification BSE image of (<b>a</b>).</p>
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<p>Plan view SEM-BSE images of the wear scars and their corresponding 3D surface morphologies and cross-sectional profiles under the normal load of 70 N after fretting cycles of 24 × 10<sup>3</sup> (<b>a</b>–<b>c</b>), 48 × 10<sup>3</sup> (<b>d</b>–<b>f</b>), and 72 × 10<sup>3</sup> (<b>g</b>–<b>i</b>).</p>
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<p>SEM-BSE images of the central region of the wear scars and their corresponding 3D surface morphologies under the normal load of 70 N after fretting cycles of 24 × 10<sup>3</sup> (<b>a</b>,<b>b</b>), 48 × 10<sup>3</sup> (<b>c</b>,<b>d</b>), and 72 × 10<sup>3</sup> (<b>e</b>,<b>f</b>), and the higher magnification SEM-BSE image corresponding to the rectangular area.</p>
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29 pages, 2803 KiB  
Article
Extraction Chromatography Materials Prepared with HDEHP on Different Inorganic Supports for the Separation of Gadolinium and Terbium
by Fabiola Monroy-Guzman, Celia del Carmen De la Cruz Barba, Edgar Jaime Salinas, Vicente Garibay-Feblés and Tobias Noel Nava Entzana
Metals 2020, 10(10), 1390; https://doi.org/10.3390/met10101390 - 19 Oct 2020
Cited by 6 | Viewed by 3861
Abstract
Bis(2-ethylhexyl)phosphoric acid (HDEHP) is frequently used as an extractant in the separation and recovery of lanthanides by solvent extraction and extraction chromatography, where HDEHP (stationary phase) is fixed on an inert support and the mobile phase is an aqueous solution. Because the results [...] Read more.
Bis(2-ethylhexyl)phosphoric acid (HDEHP) is frequently used as an extractant in the separation and recovery of lanthanides by solvent extraction and extraction chromatography, where HDEHP (stationary phase) is fixed on an inert support and the mobile phase is an aqueous solution. Because the results of extraction chromatography strongly depend on the support material, in this study, we aim to prepare solid extractants (extraction chromatography materials) with different inorganic supports impregnated with HDEHP for the adsorption of Gd and Tb from HCl solutions, putting emphasis on the effect of the supports on the solid extractant behavior. Gd and Tb partition data were determined in HCl solutions from the prepared extraction chromatography materials using elution analysis. Solid extractants were characterized by X-Ray diffraction, electron microscopy, and infrared spectroscopy in order to determine their properties and to explain their extraction behavior. The characterization of the solid extractants showed a heterogeneous distribution of the HDEHP on the surfaces of the different supports studied. The irregular shape of the support particles produces discontinuous and heterogenous silanization and HDEHP coatings on the support surface, affecting the retention performance of the solid extractant and the chromatographic resolution. Full article
(This article belongs to the Special Issue Solvent Extraction of Transition Metals)
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<p>Effect of HNO<sub>3</sub> concentration on the distribution coefficients of Gd and Tb in Ln SPS Eichrom resin [<a href="#B8-metals-10-01390" class="html-bibr">8</a>,<a href="#B25-metals-10-01390" class="html-bibr">25</a>].</p>
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<p>Elution curves of Gd and Tb separation from Ln SPS resin using HNO<sub>3</sub> and HCl as the mobile phases.</p>
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<p>Elution curves of Gd and Tb separation from Ln SPS resin using HNO<sub>3</sub> and HCl as the mobile phases.</p>
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<p>X-ray diffraction patterns, infrared spectra, and morphology of kieselguhr and kieselguhr silanized with DMCS vapors and DMCS liquid.</p>
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<p>Elution curves of Gd and Tb separation from HDEHP-impregnated kieselguhr silanized with DMCS vapors as a function of the [HDEHP] using HCl as the mobile phase.</p>
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<p>Elution curves of Gd and Tb separation from HDEHP-impregnated kieselguhr silanized with DMCS vapors as a function of the [HDEHP] using HCl as the mobile phase.</p>
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<p>Morphology, X-ray diffraction patterns, and infrared spectra of HDEHP-impregnated kieselguhr silanized with DMCS vapors as a function of the [HDEHP].</p>
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<p>Elution curves of Gd and Tb separation from HDEHP-impregnated kieselguhr silanized with DMCS vapors and DMCS liquid using HCl as the mobile phase.</p>
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<p>X-ray diffraction patterns, infrared spectra, and morphology of HDEHP (1:30)-impregnated kieselguhr silanized with DMCS vapors (KSV) and DMCS liquid (KSL).</p>
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<p>Elution curves of Gd and Tb separation from HDEHP (1:20)-impregnated volcanic rocks silanized with DMCS vapors using HCl as the mobile phase.</p>
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<p>X-ray diffraction patterns, infrared spectra, and morphology of cantera, silanized cantera with DMCS vapors, and HDEHP (1:20)-impregnated cantera.</p>
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<p>X-ray diffraction patterns, infrared spectra, and morphology of chiluca, silanized chiluca with DMCS vapors, and HDEHP (1:20)-impregnated chiluca.</p>
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<p>X-ray diffraction patterns, infrared spectra, and morphology of tezontle, silanized tezontle with DMCS vapors, and HDEHP (1:20)-impregnated tezontle.</p>
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<p>X-ray diffraction patterns, infrared spectra, and morphology of tezontle, silanized tezontle with DMCS vapors, and HDEHP (1:20)-impregnated tezontle.</p>
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<p>Elution curves of Gd and Tb separation from HDEHP (1:20)-impregnated alumina silanized with DMCS vapors using HCl as the mobile phase.</p>
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<p>X-ray diffraction patterns, infrared spectra, and morphology of alumina, silanized alumina with DMCS vapors, and HDEHP (1:20)-impregnated alumina.</p>
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<p>Elution curves of Gd and Tb separation from HDEHP (1:20)-impregnated fluorite silanized with DMCS vapors using HCl as the mobile phase.</p>
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<p>X-ray diffraction patterns, infrared spectra, and morphology of fluorite, silanized fluorite with DMCS vapors, and HDEHP (1:20)-impregnated fluorite.</p>
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<p>Mechanisms of hydrophobization, silanization, and loading of HDEHP on to supports.</p>
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19 pages, 4233 KiB  
Article
A 1D Analytical Model for Slag Infiltration during Continuous Casting of Steel under Non-Sinusoidal Mold Oscillation
by Hyunjin Yang
Metals 2020, 10(10), 1389; https://doi.org/10.3390/met10101389 - 19 Oct 2020
Cited by 4 | Viewed by 2457
Abstract
A 1D analytical model for slag infiltration during continuous casting of steel is developed to investigate the slag behavior in the mold–strand gap. The superposition principle and Fourier expansion are applied to obtain the analytical solution for transient slag flow under arbitrary mold [...] Read more.
A 1D analytical model for slag infiltration during continuous casting of steel is developed to investigate the slag behavior in the mold–strand gap. The superposition principle and Fourier expansion are applied to obtain the analytical solution for transient slag flow under arbitrary mold oscillation including non-sinusoidal oscillation mode. The validated model using literature data partially explains several controversies such as slope of slag film channel, mechanism of non-sinusoidal mold oscillation, and timing of slag infiltration. The model shows that a converging slag film into the casting direction is required to open the mold–strand gap if compression is applied in between. Also, model calculations imply that higher slag consumption is achievable from non-sinusoidal mold oscillation by means of the increase of film thickness through longer positive pressure with higher peak pressure. The model demonstrates a time difference between slag flow and pressure near the meniscus and the discrepancy in timing of infiltration between previous works is attributed to the mismatch. The model provides a concise but reliable tool to understand slag infiltration behavior and design mold oscillation settings. Full article
(This article belongs to the Special Issue Mold and Tundish Metallurgy)
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<p>(<b>a</b>) Schematic of continuous casting and (<b>b</b>) magnified view in mold–strand gap (not scaled).</p>
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<p>Velocity and pressure profiles in converging slag film during mold oscillation cycle: (<b>a</b>) At downstroke, (<b>b</b>) at upstroke.</p>
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<p>Velocity and pressure profiles in diverging slag film during mold oscillation cycle: (<b>a</b>) At downstroke, (<b>b</b>) at upstroke.</p>
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<p>Transition of velocity profile in liquid slag film during mold oscillation cycle.</p>
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<p>Schematic of simulation domain.</p>
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<p>Flow chart for the analytical model algorithm.</p>
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<p>(<b>a</b>) Mold displacement and (<b>b</b>) velocity for Case A2, A3, and A4 during each oscillation cycle.</p>
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<p>Transient velocity profiles at the center of slag film (<span class="html-italic">x</span> = <span class="html-italic">L</span>/2) during the oscillation cycle: (<b>a</b>) A2 (sinusoidal oscillation), (<b>b</b>) A4 (non-sinusoidal oscillation with modification ratio <math display="inline"><semantics> <mrow> <mi>α</mi> <mo>=</mo> <mn>24</mn> <mo>%</mo> </mrow> </semantics></math>).</p>
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<p>Comparison of velocity profiles at top (<span class="html-italic">x</span> = 0) and bottom (<span class="html-italic">x</span> = <span class="html-italic">L</span>) of film channel in Case A2.</p>
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<p>(<b>a</b>) Slag consumption <math display="inline"><semantics> <mrow> <msub> <mi>Q</mi> <mrow> <mi>l</mi> <mi>u</mi> <mi>b</mi> </mrow> </msub> </mrow> </semantics></math> and (<b>b</b>) force from slag pressure during the oscillation cycle.</p>
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<p>(<b>a</b>) Liquid film thickness, slope of the film, and (<b>b</b>) slag consumption with different modification ratio for non-sinusoidal mold oscillation (Case A1–A10).</p>
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<p>(<b>a</b>) Liquid film thickness, slope of the film, and (<b>b</b>) slag consumption with different casting speed (Case B1–B11).</p>
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<p>(<b>a</b>) Transient slag consumption <math display="inline"><semantics> <mrow> <msub> <mi>Q</mi> <mrow> <mi>l</mi> <mi>u</mi> <mi>b</mi> </mrow> </msub> </mrow> </semantics></math> and (<b>b</b>) force profiles from slag pressure with different modification factors <math display="inline"><semantics> <mi>α</mi> </semantics></math> during the oscillation cycle.</p>
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<p>(<b>a</b>) Normalized slag consumption during the oscillation cycle with different Fourier numbers and (<b>b</b>) transient velocity profiles for <math display="inline"><semantics> <mrow> <mi>F</mi> <mi>o</mi> </mrow> </semantics></math> = 0.027 at meniscus (x = 0).</p>
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<p>(<b>a</b>) Normalized slag consumption during the oscillation cycle with different thickness ratios (<math display="inline"><semantics> <mrow> <msub> <mi>h</mi> <mn>1</mn> </msub> <mrow> <mo>(</mo> <mrow> <mi>x</mi> <mo>=</mo> <mn>0</mn> </mrow> <mo>)</mo> </mrow> </mrow> </semantics></math>/<math display="inline"><semantics> <mrow> <msub> <mi>h</mi> <mn>2</mn> </msub> <mrow> <mo>(</mo> <mrow> <mi>x</mi> <mo>=</mo> <mi>L</mi> </mrow> <mo>)</mo> </mrow> </mrow> </semantics></math>) and (<b>b</b>) transient velocity profiles for <math display="inline"><semantics> <mrow> <msub> <mi>h</mi> <mn>1</mn> </msub> <mo>/</mo> <msub> <mi>h</mi> <mn>2</mn> </msub> </mrow> </semantics></math> = 4.5 at meniscus (<span class="html-italic">x</span> = 0).</p>
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14 pages, 2614 KiB  
Article
The Role of Surfactant Structure on the Development of a Sustainable and Effective Cutting Fluid for Machining Titanium Alloys
by Elisabet Benedicto, Eva María Rubio, Diego Carou and Coral Santacruz
Metals 2020, 10(10), 1388; https://doi.org/10.3390/met10101388 - 19 Oct 2020
Cited by 16 | Viewed by 3419
Abstract
In cutting operations of titanium alloys, most of the problems are related to the high consumption of cutting tools due to excessive wear. An improvement of metalworking fluid (MWF) technology would increase the productivity, sustainability, and quality of machining processes by lubricating and [...] Read more.
In cutting operations of titanium alloys, most of the problems are related to the high consumption of cutting tools due to excessive wear. An improvement of metalworking fluid (MWF) technology would increase the productivity, sustainability, and quality of machining processes by lubricating and cooling. In this research article, the authors varied the surfactant’s charge, the hydrocarbon chain length, and the ethoxylation degree. Surfactants were dispersed at 1.2 mM in water and trimethylolpropane oleate to produce water-based MWF. Infrared reflection absorption spectroscopy and total organic carbon analysis were used to study the influence of surfactant structure on the film forming ability of the emulsion and performance was studied on Ti6Al4V using tapping torque test. The results showed that by changing the molecular structure of the surfactant, it is possible to vary the affinity between the ester and the substrate and reach an optimal combination, which improves the formation of a tribofilm. The mixture with anionic surfactants has good tribology performance, while non-ionic surfactants shorten the tool’s life. Moreover, the increase in the hydrocarbon chain length and the number of ethoxylations of surfactants promotes the adhesion of ester onto the metal surface, improving the lubricity properties of environmentally friendly MWF. Full article
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<p>Test set-up diagram to study the role of surfactant structure on the ability to build up a lubricating film.</p>
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<p>Determination of fatty acid ester on metal surface: (<b>a</b>) spectrum of an emulsion with the C=O characteristic peak of an esters; (<b>b</b>) Iraffinity-1S (Shimadzu, Nagoya, Japan); (<b>c</b>) calibration curve.</p>
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<p>Experimental setup: tribological test using a tapping torque test system with Ti6Al4V workpiece.</p>
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<p>Measurement of the tapping torque during cutting.</p>
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<p>Amount of fatty acid ester adhered on titanium alloy strips after treatment with several emulsions. Points correspond to the first tapping torque value (TTT) for each emulsion.</p>
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<p>Tool life: (<b>a</b>) new cutting tool; (<b>b</b>) cutting tool after 15 cuts with an anionic surfactant emulsion; (<b>c</b>) broken tool after tapping with a non-ionic surfactant emulsion.</p>
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<p>Evolution of the tapping torque with machining of consecutive cuttings: anionic with continuous line and non-ionic with dashed line.</p>
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<p>Evolution of the tapping torque with machining of consecutive cuttings: anionic with continuous line and non-ionic with dashed line.</p>
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<p>Difference in tapping torque between the first and fifth cut versus carbon chain length.</p>
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<p>Organic matter adhered on Ti4Al4V strips treated with formulations containing different anionic surfactants with different ethoxylations against its lubricity performance.</p>
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8 pages, 4043 KiB  
Article
Effect of Quasi-Hydrostatic Pressure on Deformation Mechanism in Ti-10Mo Alloy
by Baozhen Jiang, Satoshi Emura and Koichi Tsuchiya
Metals 2020, 10(10), 1387; https://doi.org/10.3390/met10101387 - 17 Oct 2020
Cited by 3 | Viewed by 2032
Abstract
The deformation mechanisms of Ti-10Mo (wt.%) alloy subjected to different quasi-hydrostatic pressure values were investigated under constrained compression using stage of high-pressure torsion apparatus. Deformation products contain {332}<113> mechanical twinning, stress-induced α″ martensitic phase and stress-induced ω phase. A volume expansion accompanied stress-induced [...] Read more.
The deformation mechanisms of Ti-10Mo (wt.%) alloy subjected to different quasi-hydrostatic pressure values were investigated under constrained compression using stage of high-pressure torsion apparatus. Deformation products contain {332}<113> mechanical twinning, stress-induced α″ martensitic phase and stress-induced ω phase. A volume expansion accompanied stress-induced α″ martensitic phase transformation is 2.06%. By increasing the applied pressure from 2.5 GPa to 5 GPa, the dominant deformation mechanism underwent a transition from stress-induced α″ martensitic phase transformation to {332}<113> mechanical twinning. Full article
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<p>(<b>a</b>) EBSD inverse pole figure map of Ti-10Mo alloy after solution treatment, (<b>b</b>) dark field image of athermal ω phase and the corresponding SAED pattern along [011]<sub>β</sub> zone axis.</p>
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<p>XRD spectrums for specimens compressed at different hydrostatic pressures.</p>
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<p>EBSD and TEM analysis of the specimen compressed at a hydrostatic pressure of 2.5 GPa: (<b>a</b>) EBSD inverse pole figure map of β phase, (<b>b</b>) EBSD inverse pole figure map of SIM α″ phase, (<b>c</b>) line traces across the region indicated by white arrows in (<b>a</b>) showing the misorientation angle, (<b>d</b>) dark field image of SIM α″ phase and (<b>e</b>) the corresponding SAED pattern.</p>
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<p>EBSD and TEM analysis of the specimen compressed at a hydrostatic pressure of 5 GPa: (<b>a</b>) EBSD inverse pole figure map of β phase, (<b>b</b>) EBSD inverse pole figure map of SIM α″ phase, (<b>c</b>) line traces across the region indicated by white arrows in (<b>a</b>) showing the misorientation angle, (<b>d</b>) dark field image of primary {332}&lt;113&gt; twin, (<b>e</b>) the corresponding SAED pattern illustrates twinning plane and twinning axis of primary {332}&lt;113&gt; twin, (<b>f</b>) dark field image of secondary {332}&lt;113&gt; twins, (<b>g</b>) the corresponding SAED pattern illustrates twinning plane and twinning axis of secondary {332}&lt;113&gt; twins, (<b>h</b>) dark field image of ω phase in the matrix and the corresponding SAED pattern and (<b>i</b>) dark field image of ω phase in the primary {332}&lt;113&gt; twin and the corresponding SAED pattern. The subscripts “M”, “Pt” and “St” denote β matrix, primary twin and secondary twin, respectively.</p>
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18 pages, 3889 KiB  
Article
A New Nodal-Integration-Based Finite Element Method for the Numerical Simulation of Welding Processes
by Yabo Jia, Jean-Michel Bergheau, Jean-Baptiste Leblond, Jean-Christophe Roux, Raihane Bouchaoui, Sebastien Gallée and Alexandre Brosse
Metals 2020, 10(10), 1386; https://doi.org/10.3390/met10101386 - 17 Oct 2020
Cited by 11 | Viewed by 2974
Abstract
This paper aims at introducing a new nodal-integration-based finite element method for the numerical calculation of residual stresses induced by welding processes. The main advantage of the proposed method is to be based on first-order tetrahedral meshes, thus greatly facilitating the meshing of [...] Read more.
This paper aims at introducing a new nodal-integration-based finite element method for the numerical calculation of residual stresses induced by welding processes. The main advantage of the proposed method is to be based on first-order tetrahedral meshes, thus greatly facilitating the meshing of complex geometries using currently available meshing tools. In addition, the formulation of the problem avoids any locking phenomena arising from the plastic incompressibility associated with von Mises plasticity and currently encountered with standard 4-node tetrahedral elements. The numerical results generated by the nodal approach are compared to those obtained with more classical simulations using finite elements based on mixed displacement–pressure formulations: 8-node Q1P0 hexahedra (linear displacement, constant pressure) and 4-node P1P1 tetrahedra (linear displacement, linear pressure). The comparisons evidence the efficiency of the nodal approach for the simulation of complex thermal–elastic–plastic problems. Full article
(This article belongs to the Special Issue Advanced Computational Modeling of Metal Transformation Processes)
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<p>Multiphysics couplings during welding processes. Dotted arrows denote effects disregarded most of the time.</p>
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<p>Definition of nodal subdomains in 2D and 3D.</p>
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<p>Couplings between a node and its first- and second-neighbors.</p>
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<p>Diagram of the 3-pass slot weld sample.</p>
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<p>Meshes— (<b>a</b>) hexaheral mesh (27,000 3D elements/29,000 nodes), (<b>b</b>) free tetrahedral mesh (129,277 3D elements/24,865 nodes), (<b>c</b>) free tetrahedral mesh (163,798 3D elements/34,588 nodes); Top: global-meshes—Middle: 2D sections—Bottom: zooms on the weld zone.</p>
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<p>Temperature distributions calculated at <math display="inline"><semantics> <mrow> <mi>t</mi> <mo>=</mo> <mn>34</mn> <mspace width="0.166667em"/> <mi mathvariant="normal">s</mi> </mrow> </semantics></math> with (<b>a</b>) mesh A, (<b>b</b>) mesh B, (<b>c</b>) mesh C.</p>
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<p>Young’s modulus, thermal strain, and hardening curves of the AISI 316 stainless steel.</p>
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<p>Longitudinal <math display="inline"><semantics> <msub> <mi>σ</mi> <mrow> <mi>y</mi> <mi>y</mi> </mrow> </msub> </semantics></math> residual stress for (<b>a</b>) Q1P0 elements, (<b>b</b>) P1P1 elements with mesh B, (<b>c</b>) P1P1 elements with mesh C, (<b>d</b>) nodal approach with mesh B, (<b>e</b>) nodal approach with mesh C (unit: MPa) at <span class="html-italic">t =</span> 1000 s.</p>
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<p>Comparison of residual stresses <math display="inline"><semantics> <msub> <mi>σ</mi> <mrow> <mi>x</mi> <mi>x</mi> </mrow> </msub> </semantics></math> and <math display="inline"><semantics> <msub> <mi>σ</mi> <mrow> <mi>y</mi> <mi>y</mi> </mrow> </msub> </semantics></math> in depth.</p>
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<p>Mean stress obtained on mesh B with various options for the calculation of nodal thermal strains—(<b>a</b>) modal temperature, (<b>b</b>) nodal subvolume averaging, (<b>c</b>) element averaging.</p>
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<p>Mean stress distributions—(<b>a</b>) Mesh A with elements Q1P0, (<b>b</b>) nodal approach with smoothed results.</p>
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13 pages, 21052 KiB  
Article
A Study on Cross-Shaped Structure of Invar Material Using Cold Wire Laser Fillet Welding (PART I: Feasibility Study for Weldability)
by Du-Song Kim, Changmin Pyo, Jaewoong Kim, Jisun Kim and Hee-Keun Lee
Metals 2020, 10(10), 1385; https://doi.org/10.3390/met10101385 - 17 Oct 2020
Cited by 8 | Viewed by 3223
Abstract
With the need for eco-friendly energy increasing rapidly due to global environmental issues, there is a rapidly increasing demand for liquefied natural gas (LNG). LNG is liquefied at minus 163 degrees Celsius, and its volume decreases to 1/600, giving it a relatively higher [...] Read more.
With the need for eco-friendly energy increasing rapidly due to global environmental issues, there is a rapidly increasing demand for liquefied natural gas (LNG). LNG is liquefied at minus 163 degrees Celsius, and its volume decreases to 1/600, giving it a relatively higher storage and transport efficiency than gaseous natural gas (NG). The material for the tanks that store cryogenic LNG must be a material with high impact toughness at cryogenic temperatures. Invar, which contains 36% nickel and has a very low coefficient of thermal expansion, is used for the membranes and corner structures of LNG cargo holds. The cross-shaped Invar structure used in an LNG cargo hold is manufactured through manual tungsten inert gas (TIG) fillet welding, which causes welding distortion and weldability problems. This study is a feasibility study that aims to reduce welding distortion, increase weldability with welding speed, and reduce the steps in an existing process by half by replacing the existing manufacturing method with automatic fiber laser fillet welding. Laser welding using fiber laser parameters are controlled for 1.5 and 3.0 mm thick Invar materials and weldability is secured through cross-section observation. Then, the optimal welding conditions with top and back beads secured are derived through a trial and error method. Full article
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<p>Experimental schematic diagram and welding location. (<b>a</b>) Isometric view of specimen (<b>b</b>) Position of fiber laser welding (<b>c</b>) Position of TIG welding.</p>
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<p>Shape of laser welding jigs.</p>
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<p>Fiber laser equipment.</p>
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<p>Optical microscope equipment and example of cross-section examination.</p>
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<p>Definition of experiment laser welding conditions. (Focal length: Distance from the center of the lens to the focal point; Working angle: Angle between the welding unit and a horizontal plate; Beam location: Distance from focal point to the corner between the horizontal plate and vertical plate; Gap: Distance from vertical plate to the edge of the horizontal plate).</p>
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<p>Difference among working angles.</p>
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<p>Differences among laser powers.</p>
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<p>Different wire feeding speeds with 1.75 kW of laser power.</p>
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<p>Different wire feeding speeds with 2.0 kW of laser power.</p>
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<p>Final result of 1.5 mm thickness Invar.</p>
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<p>Applying different levels of laser power.</p>
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<p>Applying different levels of laser power with 0.5 mm beam location.</p>
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<p>Applying different levels of laser power with 1.0 mm beam location.</p>
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<p>Different wire feeding speeds with 0.25 mm beam location.</p>
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<p>Different wire feeding speeds with 0.5 mm beam location.</p>
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<p>Final result of 3.0 mm thickness Invar.</p>
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29 pages, 8426 KiB  
Review
Corrosion of Cast Aluminum Alloys: A Review
by C. Berlanga-Labari, M. V. Biezma-Moraleda and Pedro J. Rivero
Metals 2020, 10(10), 1384; https://doi.org/10.3390/met10101384 - 16 Oct 2020
Cited by 61 | Viewed by 12661
Abstract
Research on corrosion resistance of cast aluminum alloys is reviewed in this article. The effect of the main microstructural features of cast aluminum alloys such as secondary dendrite arm spacing (SDAS), eutectic silicon morphology, grain size, macrosegregation, microsegregation, and intermetallic compounds is discussed. [...] Read more.
Research on corrosion resistance of cast aluminum alloys is reviewed in this article. The effect of the main microstructural features of cast aluminum alloys such as secondary dendrite arm spacing (SDAS), eutectic silicon morphology, grain size, macrosegregation, microsegregation, and intermetallic compounds is discussed. Moreover, the corrosion resistance of cast aluminum alloys obtained by modern manufacturing processes such as semi-solid and additive manufacturing are analyzed. Finally, the protective effects provided by different coatings on the aluminum cast alloys—such as anodized, plasma electrolytic oxidation (PEO), and laser—is reviewed. Some conclusions and future guidelines for future works are proposed. Full article
(This article belongs to the Section Corrosion and Protection)
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<p>(<b>a</b>) Typical macrostructure of an Al–6 wt %, Cu–1 wt % Si alloy, (<b>b</b>) representation of the transverse surface samples used in the corrosion tests, and (<b>c</b>) experimental and simulated Cu and Si profiles corresponding to positions close to the casting surface highlighting the Cu macrosegregation. Reprinted with permission of [<a href="#B2-metals-10-01384" class="html-bibr">2</a>].</p>
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<p>SEM micrographs and EDS analysis performed in (<b>a</b>) AlSi<sub>7</sub>Mg and (<b>b</b>) AlSi<sub>10</sub>Mg, respectively. Reprinted with permission of [<a href="#B4-metals-10-01384" class="html-bibr">4</a>].</p>
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<p>Microstructure images of A356 cast samples with different Sr addition (<b>a</b>) No Sr addition, (<b>b</b>) 120 ppm, (<b>c</b>) 170 ppm, and (<b>d</b>) 250 ppm. Reprinted with permission of [<a href="#B5-metals-10-01384" class="html-bibr">5</a>].</p>
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<p>(<b>a</b>) Change in corrosion density as a function of immersion time. (<b>b</b>) Schematic presentation of oxide layer formation at the surface of AA EN-AlSi7Mg0.3 during the course of immersion in artificial sea water with added Na<sub>2</sub>S. Reprinted with permission of [<a href="#B7-metals-10-01384" class="html-bibr">7</a>].</p>
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<p>SEM micrographs of the initial stages of corrosion attack of A356 (<b>a</b>,<b>b</b>) and A356Nd (<b>c</b>,<b>d</b>) alloys as a function of time: (<b>a</b>,<b>c</b>) 1 h, (<b>b</b>,<b>d</b>) 8 h. Reprinted with permission of [<a href="#B9-metals-10-01384" class="html-bibr">9</a>].</p>
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<p>Weight loss rate curves of ADC12-xYb aluminum alloys immersed in 3.5 wt % NaCl solution for 10, 20, 30 days. Reprinted with permission from Elsevier [<a href="#B11-metals-10-01384" class="html-bibr">11</a>].</p>
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<p>Micrographs of the AlSiCu alloy injected at different combinations of temperature and pressure (<b>a</b>) 579 °C/35 MPa, (<b>b</b>) 579 °C/70 MPa, (<b>c</b>) 643 °C/35 MPa, (<b>d</b>) 643 °C/70 MPa, (<b>e</b>) 709 °C/35 MPa, and (<b>f</b>) 709 °C/70 MPa, respectively. Reprinted with permission of [<a href="#B15-metals-10-01384" class="html-bibr">15</a>].</p>
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<p>(<b>a</b>) Macrostructure representation at CET and (<b>b</b>) average values of secondary dendrite arm spacing for Al–5 wt-%Cu and Al–8 wt-%Cu alloys. Reprinted with permission of [<a href="#B18-metals-10-01384" class="html-bibr">18</a>].</p>
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<p>Scanning electron micrographs of the cross section of the RRA B206 aluminum alloy after m 48 h of immersion in artificial seawater showing exfoliation corrosion for a scale bar of 40 µm (<b>a</b>) and 30 µm (<b>b</b>,<b>c</b>). Reprinted with permission of [<a href="#B21-metals-10-01384" class="html-bibr">21</a>].</p>
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<p>Optical micrographs of cast aluminum alloys after corrosion tests. Reprinted with permission of [<a href="#B23-metals-10-01384" class="html-bibr">23</a>].</p>
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<p>(<b>a</b>) Typical macrostructure of the as-cast Al–5 wt % Ni alloy and schematic representation of positions from where the samples were extracted for corrosion tests and (<b>b</b>) optical micrographs with corresponding dendritic spacings (<span class="html-italic">λ</span><sub>1</sub> and <span class="html-italic">λ</span><sub>2</sub> are the primary and secondary dendritic spacings, respectively) and cooling rates. Reprinted with permission of [<a href="#B24-metals-10-01384" class="html-bibr">24</a>].</p>
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<p>Cyclic polarization curves of A356-GC and A-356-RC aluminum alloys after 1 h immersion in 3.5% NaCl naturally aerated solution. Reprinted with permission of [<a href="#B41-metals-10-01384" class="html-bibr">41</a>].</p>
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<p>Corroded surfaces of (<b>a</b>) 2.5RG and (<b>b</b>) 4.5 RG after polarization test in the diluted Harrison solution. Reprinted with permission of [<a href="#B43-metals-10-01384" class="html-bibr">43</a>].</p>
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<p>Schematic illustrations showing the corrosion behavior in Al–12Si as-prepared SLM, heat-treated SLM, and the cast samples under acidic environment. Reprinted with permission of [<a href="#B75-metals-10-01384" class="html-bibr">75</a>].</p>
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<p>FIB-SEM micrograph of the corroded area in cross-section taken from the anodized sample by liquid casting. Reprinted with permission of [<a href="#B98-metals-10-01384" class="html-bibr">98</a>].</p>
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<p>Microstructures of samples: (<b>a</b>) alloy A (2.43 wt % Si), high cooling rate; (<b>b</b>) alloy C (5.45 wt % Si), high cooling rate; (<b>c</b>) alloy C M (5.45 wt % Si), high cooling rate; (<b>d</b>) alloy C M (5.45 wt % Si), low cooling rate. Reprinted with permission of [<a href="#B99-metals-10-01384" class="html-bibr">99</a>].</p>
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<p>STEM-EDXS micrographs of the anodized layer containing Si flakes (alloy C): (<b>a</b>) STEM micrograph; (<b>b</b>) EDXS elemental map. Reprinted with permission of [<a href="#B99-metals-10-01384" class="html-bibr">99</a>].</p>
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<p>High magnification STEM micrographs of Si flakes inside oxide layer: (<b>a</b>) STEM micrograph; (<b>b</b>) bulk plasmon energy map of the selected area highlighting the oxide regions; (<b>c</b>) bulk plasmon energy map of the selected area highlighting the elemental Si and Al domains. Reprinted with permission of [<a href="#B99-metals-10-01384" class="html-bibr">99</a>].</p>
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<p>Corrosion rate for coated and uncoated A356.0 substrates after 120 h immersion as determined by weight loss experiments. Reprinted with permission of [<a href="#B108-metals-10-01384" class="html-bibr">108</a>].</p>
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<p>Schematic presentation of the self-sealing mechanism of zirconium conversion coating applied on AlSi7Mg0.3 during its immersion in 0.5 M NaCl solution. Reprinted with permission of [<a href="#B109-metals-10-01384" class="html-bibr">109</a>].</p>
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13 pages, 641 KiB  
Article
Softening of Shear Elastic Coefficients in Shape Memory Alloys Near the Martensitic Transition: A Study by Laser-Based Resonant Ultrasound Spectroscopy
by Petr Sedlák, Michaela Janovská, Lucie Bodnárová, Oleg Heczko and Hanuš Seiner
Metals 2020, 10(10), 1383; https://doi.org/10.3390/met10101383 - 16 Oct 2020
Cited by 10 | Viewed by 2362
Abstract
We discuss the suitability of laser-based resonant ultrasound spectroscopy (RUS) for the characterization of soft shearing modes in single crystals of shape memory alloys that are close to the transition temperatures. We show, using a numerical simulation, that the RUS method enables the [...] Read more.
We discuss the suitability of laser-based resonant ultrasound spectroscopy (RUS) for the characterization of soft shearing modes in single crystals of shape memory alloys that are close to the transition temperatures. We show, using a numerical simulation, that the RUS method enables the accurate determination of the c shear elastic coefficient, even for very strong anisotropy, and without being sensitive to misorientations of the used single crystal. Subsequently, we apply the RUS method to single crystals of three typical examples of shape memory alloys (Cu-Al-Ni, Ni-Mn-Ga, and NiTi), and discuss the advantages of using the laser-based contactless RUS arrangement for temperature-resolved measurements of elastic constants. Full article
(This article belongs to the Special Issue Shape Memory Alloys 2020)
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<p>Simulated errors in <math display="inline"><semantics> <msup> <mi>c</mi> <mo>′</mo> </msup> </semantics></math> resulting from a small misorentation of the sample: (<b>a</b>) methods based on time-of-flight measurements; (<b>b</b>) resonant ultrasound spectroscopy. The misorientation angle <math display="inline"><semantics> <mi>ψ</mi> </semantics></math> is defined in the sketch on the very left.</p>
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<p>Evolution of the elastic constant <math display="inline"><semantics> <msup> <mi>c</mi> <mo>′</mo> </msup> </semantics></math> (<b>a</b>) and the internal friction parameter (<b>b</b>) for the CuAlNi single crystal.</p>
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<p>Evolution of the elastic constant <math display="inline"><semantics> <msup> <mi>c</mi> <mo>′</mo> </msup> </semantics></math> for the Ni-Mn-Ga samples: (<b>a</b>) sample No.2 with the transition temperature below the Curie point <math display="inline"><semantics> <msub> <mi>T</mi> <mi>C</mi> </msub> </semantics></math>; (<b>b</b>) sample No.3 with the transition temperature above the curie point. In (<b>a</b>), the constants <math display="inline"><semantics> <msup> <mi>c</mi> <mo>′</mo> </msup> </semantics></math> for two tetragonal variants of martensite V1 and V2 are effective elastic constants only, obtained under the assumption that the material has a cubic symmetry (see the text for more details); the dash-dot line is the extrapolation of the behavior of austenite above the Curie point. In (<b>b</b>), the <math display="inline"><semantics> <msup> <mi>c</mi> <mo>′</mo> </msup> </semantics></math> below <math display="inline"><semantics> <msub> <mi>A</mi> <mi>S</mi> </msub> </semantics></math> is again an effective parameter, representing the initial mixture of variants. Note the different temperature scales between (<b>a</b>,<b>b</b>).</p>
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<p>(<b>a</b>) the misorientation between the sample edges (<math display="inline"><semantics> <msub> <mi>y</mi> <mrow> <mn>1</mn> <mo>,</mo> <mo>…</mo> <mo>,</mo> <mn>3</mn> </mrow> </msub> </semantics></math>) and the principal <math display="inline"><semantics> <mrow> <mo>〈</mo> <mn>1</mn> <mspace width="0.166667em"/> <mn>0</mn> <mspace width="0.166667em"/> <mn>0</mn> <mo>〉</mo> </mrow> </semantics></math> directions. The map plotted on the unit sphere is a map of a function used for determination of the symmetry planes of the material for the measured 21 (triclinic) elastic constants, as introduced in [<a href="#B21-metals-10-01383" class="html-bibr">21</a>]. In particular, the sharp minima (blue spots) correspond to directions perpendicular to the mirror planes. (<b>b</b>) the resulting evolution of the elastic constants.</p>
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14 pages, 1768 KiB  
Article
First Experimental Values for the Light Penetration Depth of Platinum and Iron Gases at 532 nm
by Gonzalo Rodríguez Prieto and Luis Bilbao
Metals 2020, 10(10), 1382; https://doi.org/10.3390/met10101382 - 16 Oct 2020
Viewed by 2632
Abstract
Light penetration depth is a fundamental property that has been researched extensively with a large amount of materials. Among those studies, different planetary atmospheres and material phases, like plasmas, had been previously addressed, both theoretically and experimentally. However, no experimental data are available [...] Read more.
Light penetration depth is a fundamental property that has been researched extensively with a large amount of materials. Among those studies, different planetary atmospheres and material phases, like plasmas, had been previously addressed, both theoretically and experimentally. However, no experimental data are available for platinum and iron gases due to the difficulties for the creation of gas state from a solid metal material. This work present experimental penetration depths at 532 nm laser light for iron and platinum gases produced by a carefully tuned exploding wire system in atmospheric air. Iron presents a larger dispersion on the data than platinum, which is explained because of its large magnetic permeability value, that generates a less homogeneous gas than in the platinum case. Full article
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<p>(Color online) experimental setup. PH1 signals the photodiode, C the capacitors bank, <math display="inline"><semantics> <msub> <mi>L</mi> <mn>0</mn> </msub> </semantics></math> the lumped inductance, 142 nHr, and <math display="inline"><semantics> <msub> <mi>R</mi> <mn>0</mn> </msub> </semantics></math> the resistance; both of the whole setup circuit.</p>
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<p>(Color online) typical current signal for these experiments. Insert on the lower left part is a false color streak image at the same time scale. Notice how the initial current instead of expanding a gas, creates it, so in the streak no large expansion is observed.</p>
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<p>(Color online) optical configuration of the streak camera and CW laser illumination system. (1) CW 532 nm laser head, (2) beam expander X10, (3) two lenses combination, (4) exploding wire and (5) streak camera and objective.</p>
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<p>(Color online) typical platinum streak images at (<b>a</b>) 10 kV, (<b>b</b>) 15 kV and (<b>c</b>) 20 kV of charging voltage in the capacitors bank. Notice the different times scale in the last case. Space (vertical dimension) scale is the same in all the images.</p>
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<p>(Color online) typical iron streak images at (<b>a</b>) 10 kV, (<b>b</b>) 15 kV and (<b>c</b>) 20 kV of charging voltage in the capacitors bank. Notice the different scales.</p>
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<p>(Color online) streak image from an iron experiment with 10 kV in the capacitors bank. Inset shows the border between the shock wave and metal gas increase at the end of its live.</p>
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<p>(Color online) streak image from an iron experiment with 15 kV in the capacitors bank. Superimposed graph shows the intensity traces at the approximate positions marked by the arrows. There are differences not only in width, but also in attenuation, with the latter getting larger as the metal gas expands and absorb more electrical energy from the capacitors.</p>
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<p>(Color online) energy absorbed (<span style="color: #FF0000">– –</span>), voltage(<span style="color: #00FF00">- -</span>), and current(<span style="color: #00AEEF">—</span>) flowing through an iron wire when charging voltage was 20 kV.</p>
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<p>(Color online) iron metal gas penetration depth aggregated by the charging voltages on the capacitors bank as function of the expansion radius squared.</p>
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<p>(Color online) penetration depth of platinum metal gas, also aggregated by charging voltages.</p>
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<p>(Color online) penetration of platinum metal gas as a function of the metal absorbed energy. Average values are shown as a guide to the eye.</p>
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<p>(Color online) iron metal gas penetration depth depending on the absorbing energy. As in the platinum case, the average of all the available data is shown.</p>
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13 pages, 7641 KiB  
Article
Determination of the Grain Size in Single-Phase Materials by Edge Detection and Concatenation
by Lucijano Berus, Plavka Skakun, Dragan Rajnovic, Petar Janjatovic, Leposava Sidjanin and Mirko Ficko
Metals 2020, 10(10), 1381; https://doi.org/10.3390/met10101381 - 16 Oct 2020
Cited by 11 | Viewed by 4157
Abstract
This paper presents a novel approach for edge detection and concatenation. It applies the proposed method on a set of optical microscopy images of aluminium alloy Al 99.5% (ENAW1050A) samples with different grain size values. The performance of the proposed approach is evaluated [...] Read more.
This paper presents a novel approach for edge detection and concatenation. It applies the proposed method on a set of optical microscopy images of aluminium alloy Al 99.5% (ENAW1050A) samples with different grain size values. The performance of the proposed approach is evaluated based on the intercept method and compared with the manual grain size determination method. Edge detection filters have proven inefficient in grain boundaries’ detection of the presented microscopy images. To some extent only the Canny edge-detection filter was able to compute grain boundaries of lower-resolution images adequately, while the presented method proved to be superior, especially in high-resolution images. The proposed method has proven its applicability, and it implies higher automatisation and lower processing times compared to manual optical microscopy image processing. Full article
(This article belongs to the Special Issue Applied Artificial Intelligence in Steelmaking)
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<p>Designations of the nine pixels in a 3 × 3 kernel [<a href="#B15-metals-10-01381" class="html-bibr">15</a>].</p>
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<p>Pseudocode and flowchart of the connecting the edges procedure.</p>
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<p>Measurement of average grain size in a material using the ASTM E1382 linear intercept method [<a href="#B20-metals-10-01381" class="html-bibr">20</a>]. Reproduced with permission from Pauli Lehto, Aalto University Wiki; published by Aalto University.</p>
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<p>The original microstructure image (<b>a</b>) contrast manipulation (<b>b</b>) with an enhancement of the picture details, while preserving edges based on a local Laplacian filter with <math display="inline"><semantics> <mrow> <mi>α</mi> <mo>=</mo> <mn>0.1</mn> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <msub> <mi>σ</mi> <mi>L</mi> </msub> <mo>=</mo> <mn>0.5</mn> </mrow> </semantics></math> and <math display="inline"><semantics> <mrow> <mi>β</mi> <mo>=</mo> <mn>0</mn> </mrow> </semantics></math>. Gaussian filtering (<b>c</b>) to blur the image with 2D 47 × 47 convolution kernel and standard deviation <math display="inline"><semantics> <mrow> <msub> <mi>σ</mi> <mi>G</mi> </msub> <mo>=</mo> <mn>8</mn> </mrow> </semantics></math>.</p>
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<p>Sobel gradient filter different threshold values <math display="inline"><semantics> <mrow> <mi>t</mi> <mi>h</mi> <mi>r</mi> <mi>e</mi> <mi>s</mi> <mi>h</mi> <mi>o</mi> <mi>l</mi> <mi>d</mi> <mn>1</mn> <mtext> </mtext> <mo>=</mo> <mtext> </mtext> <mn>20</mn> </mrow> </semantics></math> (<b>a</b>), <math display="inline"><semantics> <mrow> <mi>t</mi> <mi>h</mi> <mi>r</mi> <mi>e</mi> <mi>s</mi> <mi>h</mi> <mi>o</mi> <mi>l</mi> <mi>d</mi> <mn>2</mn> <mtext> </mtext> <mo>=</mo> <mtext> </mtext> <mn>30</mn> </mrow> </semantics></math> (<b>b</b>) in <math display="inline"><semantics> <mrow> <mi>t</mi> <mi>h</mi> <mi>r</mi> <mi>e</mi> <mi>s</mi> <mi>h</mi> <mi>o</mi> <mi>l</mi> <mi>d</mi> <mn>3</mn> <mtext> </mtext> <mo>=</mo> <mtext> </mtext> <mn>50</mn> <mtext> </mtext> </mrow> </semantics></math>(<b>c</b>).</p>
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<p>Zhang’s thinning algorithm used to compute binary edge images.</p>
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<p>Procedure for connection of the edges procedure; green regions represents binary edge (BE), image combined green and red regions represent BE+.</p>
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<p>Tested images TI1, TI2, TI3, TI4, TI5 and TI6. Image sizes vary from 724 × 724 (for TI1, TI2 and TI3) to 1536 × 1536 (for TI4, TI5 and TI6).</p>
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<p>Results of average grain size predictions of tested images TI1 to TI6, based on the conventional method, BE, BE+ and Canny edge detection filter.</p>
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<p>BE, BE+ and Canny edge detection grain size measurements with different spacing values for TI2 (<b>a</b>) and TI4 (<b>b</b>), compared to the conventional grain size determination method.</p>
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13 pages, 4216 KiB  
Article
The Effects of Reduction and Thermal Treatment on the Recrystallization and Crystallographic Texture Evolution of 5182 Aluminum Alloy
by Sofia Papadopoulou, Athina Kontopoulou, Evangelos Gavalas and Spyros Papaefthymiou
Metals 2020, 10(10), 1380; https://doi.org/10.3390/met10101380 - 16 Oct 2020
Cited by 14 | Viewed by 3163
Abstract
During forming, thickness reduction and thermal treatment affect the recrystallization and evolution of the crystallographic texture of metallic materials. The present study focuses on the consequences of rolling reduction of a widespread aluminum alloy with numerous automotive, marine and general-purpose applications, namely Al [...] Read more.
During forming, thickness reduction and thermal treatment affect the recrystallization and evolution of the crystallographic texture of metallic materials. The present study focuses on the consequences of rolling reduction of a widespread aluminum alloy with numerous automotive, marine and general-purpose applications, namely Al 5182. Emphasis is laid on the crystallographic texture and mechanical properties on both hot and cold-rolled semi-final products. In particular, a 2.8 mm-thick hot-rolled product was examined in the as-received condition, while two cold-rolled sheets, one 1.33 mm and the other 0.214 mm thick, both originating from the 2.8 mm material, were examined in both as-received and annealed (350 °C for 1 h) conditions. Electron back-scatter diffraction indicated the presence of a large percentage of random texture as well as a weak recrystallization texture for the hot-rolled product, whereas in the case of cold rolling the evolution of β-fiber texture was noted. In addition, tensile tests showed that both the anisotropy as well as the mechanical properties of the cold-rolled properties improved after annealing, being comparable to hot-rolled ones. Full article
(This article belongs to the Special Issue Structure-Properties-Processing Relationships in Metallic Materials)
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<p>The microstructure of (<b>a</b>) hot-rolled sheet, (<b>b</b>) cold-rolled 1.3 mm sheet, (<b>c</b>) cold-rolled 1.3 mm annealed sheet, (<b>d</b>) cold-rolled 0.214 mm sheet and (<b>e</b>) cold-rolled 0.214 mm annealed sheet after Barker’s etching.</p>
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<p>Scanning electron microscopy (SEM) images showing (<b>a</b>) h.r. sample and (<b>b</b>) c.r.2.</p>
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<p>Electron back-scatter diffraction (EBSD) data for the examined products.</p>
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<p>Typical textures [(111) pole figures] in different processing stages of Al-alloy sheet [<a href="#B32-metals-10-01380" class="html-bibr">32</a>].</p>
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<p>Texture percentage chart.</p>
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<p>Yield strength data for all products and conditions.</p>
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<p>Tensile strength data for all products and conditions.</p>
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<p>Elongation at fracture data for all products and conditions.</p>
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<p>The r average in relation to direction (0°, 45°, 90°).</p>
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14 pages, 5985 KiB  
Article
Influence of Scanning Strategy on the Performances of GO-Reinforced Ti6Al4V Nanocomposites Manufactured by SLM
by Xiaojin Miao, Xin Liu, Peipei Lu, Jitai Han, Weipeng Duan and Meiping Wu
Metals 2020, 10(10), 1379; https://doi.org/10.3390/met10101379 - 16 Oct 2020
Cited by 21 | Viewed by 2910
Abstract
In this work, the effects of line (L-scanning strategy), stripe (S-scanning strategy), hollow square (H-scanning strategy) and chess board partition (C-scanning strategy) on the performances of graphene oxide reinforced Ti6Al4V matrix nanocomposites (GO/TC4) as fabricated by selective laser melting (SLM) were investigated. Numerical [...] Read more.
In this work, the effects of line (L-scanning strategy), stripe (S-scanning strategy), hollow square (H-scanning strategy) and chess board partition (C-scanning strategy) on the performances of graphene oxide reinforced Ti6Al4V matrix nanocomposites (GO/TC4) as fabricated by selective laser melting (SLM) were investigated. Numerical temperature field simulation of four different scanning strategies was utilized to investigate the effects of thermal concentration on SLM-processed GO/TC4 nanocomposites, linking to its micro-voids, surface roughness, porosity, microhardness and tribological properties. The proposed simulation scheme is validated by comparing the simulated thermal analysis with experimental results. Simulation results show that the thermal concentration effects of a part during SLM process is distinctive under different scanning strategies, with the slowest cooling rate of 64,977.5 °C/s that is achieved by C-scanning strategy specimen. The experimental results indicate that the performances of the L-scanning strategy or S-scanning strategy sample are seriously affected by the thermal concentration, causing a large number of micro-voids and defects. All the experimental results suggest that the sample using C-scanning strategy exhibits the optimal performance of all investigated specimens, which closely correlates with its lowest temperature gradients. This study highlights the importance of using a partition scanning strategy during SLM process, which can be easily extended to other powder bed fusion process. Full article
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<p>Scanning electron microscope (SEM) image of graphene oxide/Ti6Al4V (GO/TC4) powder.</p>
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<p>Schematic of four different scanning strategies: (<b>a</b>) L-scanning strategy; (<b>b</b>) S-scanning strategy; (<b>c</b>) H-scanning strategy; (<b>d</b>) C-scanning strategy (scan in the order of 1–6).</p>
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<p>Melt tracks and temperature distributions of melt pool under different scanning strategies: (<b>a</b>) L-scanning strategy; (<b>b</b>) S-scanning strategy; (<b>c</b>) H-scanning strategy; (<b>d</b>) C-scanning strategy.</p>
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<p>Temperature profiles of testing points under different scanning strategies: (<b>a</b>) L-scanning strategy; (<b>b</b>) S-scanning strategy; (<b>c</b>) H-scanning strategy; (<b>d</b>) C-scanning strategy.</p>
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<p>Temperature distributions at the end of the building process after cooling for 0.00204 s: (<b>a</b>) L-scanning strategy; (<b>b</b>) S-scanning strategy; (<b>c</b>) H-scanning strategy; (<b>d</b>) C-scanning strategy.</p>
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<p>Surface topography of GO/TC4 samples under different scanning strategies: (<b>a</b>) L-scanning strategy; (<b>b</b>) S-scanning strategy; (<b>c</b>) H-scanning strategy; (<b>d</b>) C-scanning strategy.</p>
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<p>Microhardness of GO/TC4 nanocomposites under different scanning strategies.</p>
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<p>Tribological behaviors of GO/TC4 nanocomposites: (<b>a</b>) real-time friction coefficient; (<b>b</b>) average coefficient of friction; (<b>c</b>) wear volume.</p>
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<p>SEM images of worn surfaces of different samples: (<b>a</b>) L-scanning strategy; (<b>b</b>) S-scanning strategy; (<b>c</b>) H-scanning strategy; (<b>d</b>) C-scanning strategy.</p>
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12 pages, 2145 KiB  
Review
Radiation Damage of Reactor Pressure Vessel Steels Studied by Positron Annihilation Spectroscopy—A Review
by Vladimír Slugeň, Stanislav Sojak, Werner Egger, Vladimir Krsjak, Jana Simeg Veternikova and Martin Petriska
Metals 2020, 10(10), 1378; https://doi.org/10.3390/met10101378 - 16 Oct 2020
Cited by 11 | Viewed by 3177
Abstract
Safe and long term operation of nuclear reactors is one of the most discussed challenges in nuclear power engineering. The radiation degradation of nuclear design materials limits the operational lifetime of all nuclear installations or at least decreases its safety margin. This paper [...] Read more.
Safe and long term operation of nuclear reactors is one of the most discussed challenges in nuclear power engineering. The radiation degradation of nuclear design materials limits the operational lifetime of all nuclear installations or at least decreases its safety margin. This paper is a review of experimental PALS/PLEPS studies of different nuclear reactor pressure vessel (RPV) steels investigated over last twenty years in our laboratories. Positron annihilation lifetime spectroscopy (PALS) via its characteristics (lifetimes of positrons and their intensities) provides useful information about type and density of radiation induced defects. The new results obtained on neutron-irradiated and hydrogen ions implanted German steels were compared to those from the previous studies with the aim to evaluate different processes (neutron flux/fluence, thermal treatment or content of selected alloying elements) to the microstructural changes of neutron irradiated RPV steel specimens. The possibility of substitution of neutron treatment (connected to new defects creation) via hydrogen ions implantation was analyzed as well. The same materials exposed to comparable displacement damage (dpa) introduced by neutrons and accelerated hydrogen ions shown that in the results interpretation the effect of hydrogen as a vacancy-stabilizing gas must be considered, too. This approach could contribute to future studies of nuclear fission/fusion design steels treated by high levels of neutron irradiation. Full article
(This article belongs to the Special Issue Radiation Effects in Steels and Alloys)
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<p>Positron lifetimes of all measured P370 WM specimens–unirradiated, neutron irradiated (D77 and D161) and 3 levels of H<sup>+</sup> ion irradiated.</p>
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<p>Intensity of positron lifetimes of all measured P370 WM specimens–unirradiated, neutron irradiated (D77 and D161) and 3 levels of H<sup>+</sup> ion irradiated.</p>
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<p>Comparison of PLEPS parameters in two components analyze of specimen P370 WM, before and after H<sup>+</sup> implantation by 100 keV (maximal damage at about 12 keV corresponding to depth of about 400–450 nm). Lifetimes and intensities of first component are presented.</p>
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<p>Comparison of PLEPS parameters in two components analyze of specimen P370 WM, before and after H<sup>+</sup> implantation by 100 keV (maximal damage at about 12 keV corresponding to depth of about 400–450 nm). Lifetimes and intensities of second component are presented.</p>
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<p>Comparison difference of positron mean lifetimes values before and after H<sup>+</sup> implantation of specimen P370 WM to dpa and H concentration profiles derived from SRIM code.</p>
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<p>H/dpa ratio as the function of depth.</p>
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9 pages, 3068 KiB  
Article
Joining of Metal to Ceramic Plate Using Super-Spread Wetting
by Jaebong Yeon, Michiru Yamamoto, Peiyuan Ni, Masashi Nakamoto and Toshihiro Tanaka
Metals 2020, 10(10), 1377; https://doi.org/10.3390/met10101377 - 15 Oct 2020
Cited by 4 | Viewed by 3045
Abstract
Ceramic-metal composites with novel performance are desirable materials; however, differences in their properties result in difficulties in joining. In this study, the joining of metal to ceramic is investigated. We recently succeeded in causing super-spread wetting on the surface fine crevice structures of [...] Read more.
Ceramic-metal composites with novel performance are desirable materials; however, differences in their properties result in difficulties in joining. In this study, the joining of metal to ceramic is investigated. We recently succeeded in causing super-spread wetting on the surface fine crevice structures of metal surfaces produced by both laser irradiation and reduction-sintering of oxide powders. In this work, joining copper onto an Al2O3 plate was achieved by taking advantage of super-spread wetting. Fe2O3 powder was first sintered under reducing conditions to produce a microstructure which can cause super-spread wetting of liquid metal on an Al2O3 plate. A powder-based surface fine crevice structure of metallic iron with high porosity was well-formed due to the bonding of the reduced metallic iron particles. This structure was joined on an Al2O3 plate with no cracking by the formation of an FeAl2O4 layer buffering the mismatch gap between the thermal expansion coefficients of iron and Al2O3. We successfully achieved metalizing of the Al2O3 surface with copper without interfacial cracks using super-spread wetting of liquid copper through the sintered metallic iron layer on the Al2O3 plate. Then, laser irradiation was conducted on the surface of the copper-metalized Al2O3 plate. A laser-irradiated surface fine crevice structure was successfully created on the copper-metalized Al2O3 plate. Moreover, it was confirmed that the super-spread wetting of liquid tin occurred on the laser-irradiated surface fine crevice structure, finally accomplishing the joining of a copper block and the copper-metalized Al2O3. Full article
(This article belongs to the Special Issue Metal-Ceramic and Metal-Metal Interactions and Joining)
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<p>(<b>a</b>) Schematic diagram of experimental procedure; (<b>b</b>) Heating profiles used in Step 2 (blue line) of simultaneous reduction and sintering of applied Fe<sub>2</sub>O<sub>3</sub> and in Step 3 (red line) of metalizing copper.</p>
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<p>Illustration of the process used for joining experiments.</p>
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<p>(<b>a</b>) Cross-section of the powder-based surface fine crevice structure of metallic iron created on the Al<sub>2</sub>O<sub>3</sub> plate by sintering of Fe<sub>2</sub>O<sub>3</sub> powder under reducing conditions; (<b>b</b>) Magnified image of the region of interface between Fe-sintered layer and Al<sub>2</sub>O<sub>3</sub> plate.</p>
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<p>Phase diagram of FeO-Fe<sub>2</sub>O<sub>3</sub> system with oxygen pressure isobars. Reproduced with permission from [<a href="#B23-metals-10-01377" class="html-bibr">23</a>], Elsevier, 1999.</p>
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<p>Phase diagram of FeO-Al2O3 system. Reproduced with permission from [<a href="#B24-metals-10-01377" class="html-bibr">24</a>], Royal Society of Chemistry, 2002.</p>
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<p>(<b>a</b>) Appearance and (<b>b</b>) cross-section of sample after copper metalizing.</p>
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<p>(<b>a</b>) Surface and (<b>b</b>) cross-section of laser-irradiated surface fine crevice structure of metallic copper created on the surface of copper (iron contained or dissolved)-metallized Al<sub>2</sub>O<sub>3</sub> plate.</p>
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<p>(<b>a</b>) Appearance of sample after joining experiment and (<b>b</b>) cross-section of the junction.</p>
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13 pages, 2235 KiB  
Review
Research Progress in Preparation and Purification of Rare Earth Metals
by Hang Liu, Yao Zhang, Yikun Luan, Huimin Yu and Dianzhong Li
Metals 2020, 10(10), 1376; https://doi.org/10.3390/met10101376 - 15 Oct 2020
Cited by 22 | Viewed by 8158
Abstract
The purity of rare earth metals is one of the most important factors to research and develop high technique materials. However, high purity rare earth metals are not easily achieved. This review summarizes the preparation and purification methods of rare earth metals. First, [...] Read more.
The purity of rare earth metals is one of the most important factors to research and develop high technique materials. However, high purity rare earth metals are not easily achieved. This review summarizes the preparation and purification methods of rare earth metals. First, the preparation principle and process of molten salt electrolysis and metal thermal reduction are introduced. The main sources of metallic impurities and interstitial impurities in rare earth metals as well as the action mechanism of reducing the concentration of different impurities are analyzed and summarized. Then, the purification principle and process of vacuum distillation, arc melting, zone melting, and solid state electromigration are also discussed. Furthermore, the removal effect and function rule of metallic impurities and interstitial impurities in rare earth metals are outlined. Finally, the crucial issues in the development of high purity rare earth metals are put forward, and the development direction of high purity rare earth metals in future are pointed out on this basis. Full article
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<p>Schematic diagram of molten salt electrolysis.</p>
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<p>Effect of electrolysis temperature (<b>a</b>) and rate of addition (<b>b</b>) on oxygen concentration.</p>
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<p>Effect of casting method on oxygen concentration.</p>
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<p>Schematic diagram of metal thermal reduction.</p>
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<p>Schematic diagram of vacuum distillation.</p>
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<p>Vapor pressures of impurities (<b>a</b>) and rare earth elements (<b>b</b>) at 1600 °C.</p>
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<p>Schematic diagram of hydrogen plasma arc melting.</p>
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<p>Schematic diagram of plasma arc zone melting.</p>
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<p>Schematic diagram of solid state electromigration.</p>
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18 pages, 10599 KiB  
Article
Study on Deformation Characteristics and Microstructure Evolution of 2205/AH36 Bimetal Composite in a Novel Hot Forming Process
by Zhou Li, Haibo Xie, Fanghui Jia, Yao Lu, Xiangqian Yuan, Sihai Jiao and Zhengyi Jiang
Metals 2020, 10(10), 1375; https://doi.org/10.3390/met10101375 - 15 Oct 2020
Cited by 11 | Viewed by 2209
Abstract
A new hot forming process of a hot-rolled 2205 duplex stainless/AH36 low-carbon steel bimetal composite (2205/AH36 BC) was proposed in this study, using the Gleeble 3500 thermal-mechanical simulator and hot bending tools. The deformation characteristics of 2205/AH36 BC were studied by hot tensile [...] Read more.
A new hot forming process of a hot-rolled 2205 duplex stainless/AH36 low-carbon steel bimetal composite (2205/AH36 BC) was proposed in this study, using the Gleeble 3500 thermal-mechanical simulator and hot bending tools. The deformation characteristics of 2205/AH36 BC were studied by hot tensile tests at temperatures from 950 to 1250 °C and strain rates ranging from 0.01 to 1 s−1. The tensile temperature has a great influence on the peak flow stress of the bimetal composite. The main microstructure evolution mechanisms, including dynamic recovery (DRV) and dynamic recrystallization (DRX), changed with the deformation temperatures. The different strain rates and the change of strain rates during the deformation process have an influence on the flow behavior of the bimetal composite. During the hot bending process, qualified parts could be formed successfully without obvious cracks in the interfacial zone. Phase and grain orientation spread (GOS) maps of specimens after hot tensile and forming tests were obtained by the electron backscatter diffraction (EBSD) technique to study the microstructure evolution, respectively. It is found that the effect of the working temperature on microstructure evolution is larger than that of the stacking sequence for 2205/AH36 BC. The considerable geometrically necessary dislocation (GND) accumulation occurs around the interface of 2205/AH36 BC under all imposed working conditions after the hot bending process, due to the interfacial micro-defects and complex stress states. Full article
(This article belongs to the Section Metal Casting, Forming and Heat Treatment)
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<p>(<b>a</b>) Schematic illustration of the hot-rolled 2205/AH36 bimetal composite (BC), and (<b>b</b>) the observed metallography of 2205/AH36 BC.</p>
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<p>(<b>a</b>) Dog bone-shaped tensile specimens of 2205/AH36 BC, (<b>b</b>) the schematic diagram of hot tensile test installation and (<b>c</b>) the test simulator assembled with a tensile specimen.</p>
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<p>(<b>a</b>) Schematic diagram of hot bending setup, and (<b>b</b>) the test simulator assembled with a bending specimen.</p>
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<p>Stress–strain curves of 2205/AH36 BC at the range of 950–1250 °C with the strain rate of 0.01 s<sup>−1</sup>.</p>
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<p>(<b>a</b>) Stress–strain curves of 2205/AH36 BC, and (<b>b</b>) relationship curves of work hardening rate versus flow stress at the range of 0.01 s<sup>−1</sup>–1 s<sup>−1</sup> with the temperature of 950 °C.</p>
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<p>(<b>a</b>) The stress–strain curves with the strain rates of 0.01 and 0.1 s<sup>−1</sup> and changing from 0.01 to 0.1 s<sup>−1</sup> at 950 °C, and (<b>b</b>) the stress–strain curves with the strain rates of 0.01 and 0.1 s<sup>−1</sup> and changing from 0.1 to 0.01 s<sup>−1</sup> at 950 °C.</p>
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<p>(<b>a</b>) The observed zone after tests, and the phase maps: (<b>b</b>) as received, (<b>c</b>) at 950 °C–0.01 s<sup>−1</sup> and (<b>d</b>) at 1250 °C–0.01 s<sup>−1</sup>.</p>
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<p>Orientation map inverse pole figure (IPF)-Z direction, IPF and grain orientation spread (GOS) maps of tip zones at 950 °C–0.01 s<sup>−1</sup>: (<b>a</b>,<b>c</b> and <b>e</b>), and at 950 °C–1 s<sup>−1</sup>: (<b>b</b>,<b>d</b> and <b>f</b>). LAGBs = gray, HAGBs = black.</p>
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<p>(<b>a)</b> The bent model of 2205/AH36 BC, and the SEM morphology of the bent mid-section, (<b>b</b>) at 950 °C with the outside 2205 steel layer, (<b>c</b>) at 950 °C with the inside 2205 steel layer and (<b>d</b>) at 1050 °C with the outside 2205 steel layer.</p>
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<p>The phase, orientation map IPF-Z direction, IPF and GOS maps of specimens after hot bending: (<b>a1–a4</b>) at 950 °C with the outside 2205 steel layer, (<b>b1</b>–<b>b4</b>) at 950 °C with the inside 2205 steel layer and (<b>c1</b>–<b>c4</b>) at 1050 °C with the outside 2205 steel layer. LAGBs = gray, HAGBs = black.</p>
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<p>(<b>a</b>) Micro-hardness measurement scheme, (<b>b</b>–<b>e</b>) micro-hardness cartography maps of the as-received specimen, and specimens after hot bending at 950 °C with the outside 2205 layer, 950 °C with the inside 2205 layer and 1050 °C with the outside 2205 layer, and (<b>f</b>) comparison of the mean micro-hardness under different states.</p>
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<p>The loading force of specimens under different forming conditions.</p>
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<p>Position distributions of each segment with the increasing relative curvature at the hot working temperature of 950 °C: (<b>a</b>) with the outside 2205 steel layer, and (<b>b</b>) with the inside 2205 steel layer.</p>
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<p>Images of geometrically necessary dislocation (GND) density mapping of specimens after hot bending: (<b>a</b>) at 950 °C with the outside 2205 steel layer, (<b>b</b>) at 950 °C with the inside 2205 steel layer and (<b>c</b>) at 1050 °C with the outside 2205 steel layer.</p>
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<p>(<b>a</b>) Statistical distributions of GND density in the austenite phase, and (<b>b</b>) statistical distributions of GND density in the ferrite phase after hot bending at the working temperature of 950 °C with the outside 2205 steel layer.</p>
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<p>(<b>a</b>) The flow directions of different steel layers around the interface during the hot bending process, and (<b>b</b>) the distribution of the equivalent plastic strain of the bent specimen along the rolling direction.</p>
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25 pages, 7757 KiB  
Article
A New Approach for Obtaining the Compression Behavior of Anisotropic Sheet Metals Applicable to a Wide Range of Test Conditions
by Jorge Ayllón, Valentín Miguel, Alberto Martínez-Martínez, Juana Coello and Jesús Andrés Naranjo
Metals 2020, 10(10), 1374; https://doi.org/10.3390/met10101374 - 15 Oct 2020
Cited by 5 | Viewed by 2791
Abstract
The consideration of anisotropic and asymmetric tension-compression behaviour in some materials has proved to be of great importance for the modelling of plastic behaviours that allow for accurate results in sheet metal forming analysis. However, obtaining this compression behaviour of a sheet metal [...] Read more.
The consideration of anisotropic and asymmetric tension-compression behaviour in some materials has proved to be of great importance for the modelling of plastic behaviours that allow for accurate results in sheet metal forming analysis. However, obtaining this compression behaviour of a sheet metal in the principal plane directions is one of the most complex aspects from an experimental point of view. This complexity is notably increased when this behaviour needs to be analysed under high temperature conditions. This paper presents a compression test system with load application in the in-plane sheet directions which is characterised by a relative technical simplicity allowing its application under temperature conditions of up to 750 °C and different strain-rates. Due to the specific test conditions, namely the high temperature, it is not possible to use the common systems for measuring the strains involved and to obtain the stress-strain curve. Therefore, this paper proposes two methods for this purpose. The first is the performance of interrupted tests and measurement of the central cross sections. The second consists of inverse calibration using finite element simulations. The sensitivity of the proposed test methodology is validated through the characterisation, at room temperature, of the compression and tensile behaviour of six materials with different plastic deformation phenomena. In this way, the asymmetric tension-compression phenomena are accurately identified and high compression strains of around 0.3, higher than those existing in the literature, are investigated. A novel test methodology is thus established that is easily applicable for the mechanical characterisation of sheet metal at high temperature. Full article
(This article belongs to the Section Metal Casting, Forming and Heat Treatment)
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<p>(<b>a</b>) Schematic of the assembly for compression tests. (<b>b</b>) Initial and final stages of operation.</p>
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<p>(<b>a</b>) Diagram of the compression test specimen used. (<b>b</b>) Mesh used in FEM simulations.</p>
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<p>Influence of fillet radii on specimen behaviour. (<b>a</b>,<b>b</b>) Plastic strain. (<b>c</b>,<b>d</b>) Triaxiality.</p>
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<p>Distribution of the triaxiality parameter on each of the simulated samples <math display="inline"><semantics> <mrow> <mrow> <mo>(</mo> <mrow> <msub> <mi>ε</mi> <mrow> <mi>p</mi> <mi>l</mi> </mrow> </msub> <mo>=</mo> <mn>0.09</mn> </mrow> <mo>)</mo> </mrow> <mo>.</mo> </mrow> </semantics></math></p>
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<p>Mean triaxiality in the central zone during deformation.</p>
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<p>(<b>a</b>) Influence of anisotropy on the triaxiality of the central zone. (<b>b</b>) Influence of hardening on the triaxiality of the central zone.</p>
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<p>Validation of the central cross-section measurement methodology by simulation. (<b>a</b>) Variation in hardening parameter “<span class="html-italic">n</span>”. (<b>b</b>) Variation in normal anisotropy “<span class="html-italic">r</span>”.</p>
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<p>Strains measured (simulations and experimental tests) vs theoretical strains according to the use of the apparent curve procedure.</p>
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<p>Iterative procedure to obtain the Ticp2 stress-strain curve. (<b>a</b>) True stress-strain curve in each iteration. (<b>b</b>) Engineering curve in each iteration.</p>
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<p>(<b>a</b>) Ticp2 specimens before and after the compression test. (<b>b</b>) Measured central cross-sections.</p>
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<p>Tensile true stress-true strain curves obtained and extrapolation.</p>
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<p>DX52D steel. (<b>a</b>) Estimation of the average friction force. (<b>b</b>) Compressive response with and without correction of the friction. (<b>c</b>) Friction correction of points obtained by cross-section measurement. (<b>d</b>) Results obtained by biaxial correction.</p>
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<p>Compressive anisotropy values for the analysed materials. Experimental measure.</p>
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<p>Influence of considering isotropy or anisotropy in the determination of the stress-strain curve by inverse calibration.</p>
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<p>Compression test results. (<b>a</b>) DX52D. (<b>b</b>) Al 1050. (<b>c</b>) AISI 316. (<b>d</b>) TRIP 690. (<b>e</b>) Ticp2. (<b>f</b>) Ti6Al4V.</p>
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<p>(<b>a</b>) Compression true stress-strain curves obtained with both methodologies. (<b>b</b>) Compression simulations response.</p>
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<p>Influence of the hardening index, <span class="html-italic">n</span>, on the error dispersion of a measured compression curve.</p>
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<p>(<b>a</b>) Error dispersion in section measurement. (<b>b</b>) Error transferred to thickness measurement.</p>
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<p>Compressive anisotropy values for the analysed materials. Measures after thickness correction.</p>
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<p>Comparison of compression results with other authors. (<b>a</b>) DX52D Martínez et al. (2017). (<b>b</b>) TRIP690 Martínez et al. (2017). (<b>c</b>) Ticp Baral et al. (2018). (<b>d</b>) Ticp Nixon et al. (2010b).</p>
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13 pages, 9155 KiB  
Article
Effects of Extreme Thermal Shock on Microstructure and Mechanical Properties of Au-12Ge/Au/Ni/Cu Solder Joint
by Ziyi Wang, Songbai Xue, Weimin Long, Bo Wang, Jianhao Wang and Peng Zhang
Metals 2020, 10(10), 1373; https://doi.org/10.3390/met10101373 - 15 Oct 2020
Cited by 6 | Viewed by 2437
Abstract
Extreme temperature change has generally been the great challenge to spacecraft electronic components, particularly in long, periodic, deep-space exploration missions. Hence, researchers have paid more attention to the reliability of component packaging materials. In this study, the microstructure evolution on the interface of [...] Read more.
Extreme temperature change has generally been the great challenge to spacecraft electronic components, particularly in long, periodic, deep-space exploration missions. Hence, researchers have paid more attention to the reliability of component packaging materials. In this study, the microstructure evolution on the interface of Cu/Ni/Au/Au-12Ge/Au/Ni/Cu joints, as well as the effects of extreme thermal shock on mechanical properties and the fracture mode in the course of extreme thermal changes between −196 and 150 °C, have been investigated. Results revealed that the interface layers comprised of two thin layers of NiGe and Ni5Ge3 compounds after Au-12Ge solder alloy was soldered on the Au/Ni/Cu substrate. After extreme thermal shock tests, the microstructure morphology converted from scallop type to planar one due to the translation from NiGe to Ni5Ge3. Meanwhile, the thickness of interface layer hardly changed. The shear strength of the joints after 300 cycles of extreme thermal shock was 35.1 MPa, which decreased by 19.61%. The fracture location changed from the solder to solder/NiGe interface, and then to the interface of NiGe/Ni5Ge3 IMC layer. Moreover, the fracture type of the joints gradually transformed from ductile fracture mode to brittle mode during thermal shock test. Simultaneously, the formation and extension of defects, such as micro-voids and micro-cracks, were found during the process of thermal shock due to the different thermal expansion coefficient among the solder, interface layer and substrate. Full article
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<p>Phase diagram of Au-Ge alloy [<a href="#B25-metals-10-01373" class="html-bibr">25</a>] (with permission from Spring Nature, 2020).</p>
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<p>The schematic diagram of Cu/Ni/Au/Au-12Ge/Au/Ni/Cu joint.</p>
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<p>Top view of the micro-joints on Al<sub>2</sub>O<sub>3</sub> substrate.</p>
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<p>The diagram of shear test.</p>
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<p>Optical microstructure of Au-12Ge solder.</p>
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<p>Scanning electron microscopy (SEM) micrograph of Au-12Ge/Cu interface after soldering: (<b>a</b>) 1000×; (<b>b</b>) 5000×.</p>
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<p>SEM micrograph of Cu/Ni/Au/Au-12Ge/Au/Ni/Cu solder joints: (<b>a</b>) 100 cycles; (<b>b</b>) 200 cycles; (<b>c</b>) 300 cycles; (<b>d</b>) 400 cycles.</p>
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<p>The SEM image of Cu/Ni/Au/Au-12Ge/Au/Ni/Cu interfacial layer: (<b>a</b>) 100 cycles; (<b>b</b>) 200 cycles; (<b>c</b>) 300 cycles; (<b>d</b>) 400 cycles.</p>
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<p>The shear strength of Au-12Ge solder joint during thermal shock.</p>
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<p>The fracture surfaces of solder joints: (<b>a</b>) as soldered; (<b>b</b>) elemental mapping of (<b>a</b>); (<b>c</b>) after 100 cycles; (<b>d</b>) elemental mapping of (<b>c</b>); (<b>e</b>) after 200 cycles; (<b>f</b>) elemental mapping of (<b>e</b>); (<b>g</b>) after 300 cycles; (<b>h</b>) elemental mapping of (<b>g</b>); (<b>i</b>) after 400 cycles; (<b>j</b>) elemental mapping of (<b>i</b>).</p>
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<p>The fracture surfaces of solder joints: (<b>a</b>) as soldered; (<b>b</b>) elemental mapping of (<b>a</b>); (<b>c</b>) after 100 cycles; (<b>d</b>) elemental mapping of (<b>c</b>); (<b>e</b>) after 200 cycles; (<b>f</b>) elemental mapping of (<b>e</b>); (<b>g</b>) after 300 cycles; (<b>h</b>) elemental mapping of (<b>g</b>); (<b>i</b>) after 400 cycles; (<b>j</b>) elemental mapping of (<b>i</b>).</p>
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<p>The schematic illustration of shear failures in Au-12Ge/Au/Ni/Cu joints after shock: (<b>a</b>) 0 cycle; (<b>b</b>) 100 cycles; (<b>c</b>) 200 cycles; (<b>d</b>) 300 cycles; (<b>e</b>) 400 cycles.</p>
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15 pages, 5072 KiB  
Article
Estimation of Critical Dimensions for the Crack and Pitting Corrosion Defects in the Oil Storage Tank Using Finite Element Method and Taguchi Approach
by Mostafa Omidi Bidgoli, Kazem Reza Kashyzadeh, Seyed Saeid Rahimian Koloor and Michal Petru
Metals 2020, 10(10), 1372; https://doi.org/10.3390/met10101372 - 14 Oct 2020
Cited by 18 | Viewed by 3169
Abstract
Tanks play an important role in storing crude oil. Therefore, the maintenance and service life of tanks are very important for oil companies. In this regard, knowledge on the state of the critical conditions of various existing defects, such as cracks and pitting [...] Read more.
Tanks play an important role in storing crude oil. Therefore, the maintenance and service life of tanks are very important for oil companies. In this regard, knowledge on the state of the critical conditions of various existing defects, such as cracks and pitting corrosion defects, can play an essential role in providing a better service to these huge metal structures. In the present research, the basic theories relating to crack defects were discussed. Then, an oil reserve in one of the island states of the country was modeled and analyzed by considering different types of defects using Finite Element (FE) simulation. Next, the critical dimensions of cracks and corrosion holes were identified in a number of cases. Eventually, the Taguchi Approach (TA) was used to investigate the effect of different parameters related to the various defects, such as length, depth and diameter, on the maximum stress. The results indicated that the effect of the crack and pitting corrosion depth is superior to the effect of the length and diameter for defects of crack and pitting corrosion, respectively. Full article
(This article belongs to the Special Issue Localized Corrosion of Metals and Alloys)
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<p>The defect of the pitting corrosion at the bottom of an oil storage tank and a schematic of the crack in the tank with the geometric parameters studied in this research such as the length (mm), angle (degree) and depth of the crack (mm).</p>
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<p>Image of the oil storage tank that was studied in this research.</p>
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<p>Finite element model of the oil tank.</p>
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<p>The von Mises stress contour of the oil storage tank under the hydrostatic pressure in MPa.</p>
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<p>Schematic of the shell-to-solid coupling of elements.</p>
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<p>The contour of the equivalent von Mises stresses for both FE models: (<b>a</b>) Shell element only and (<b>b</b>) combination of shell and solid elements.</p>
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<p>The stress diagram in terms of depth for cracks of various lengths and angles: (<b>a</b>) length = 300 and angle = 0; (<b>b</b>) length = 400 and angle = 0; (<b>c</b>) length = 150 and angle = 45; (<b>d</b>) length = 200 and angle = 45; (<b>e</b>) length = 300 and angle 90; (<b>f</b>) length = 400 and angle = 90.</p>
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<p>The stress diagrams in terms of depth for pitting corrosions with various diameters: (<b>a</b>) diameter = 50 mm; (<b>b</b>) diameter = 100 mm; (<b>c</b>) diameter = 150 mm.</p>
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<p>The stress diagrams in terms of depth for pitting corrosions with various diameters: (<b>a</b>) diameter = 50 mm; (<b>b</b>) diameter = 100 mm; (<b>c</b>) diameter = 150 mm.</p>
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<p>Influences of the S/N and mean ratios of all parameters related to the crack defect with different angles: (<b>a</b>) zero, (<b>b</b>) 45 and (<b>c</b>) 90.</p>
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<p>Influences of the S/N and mean ratios of all parameters related to the pitting corrosion defect.</p>
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<p>(<b>a</b>) Effect of different parameters of the crack with various angles; (<b>b</b>) Impact of different parameters of the pitting corrosion defect in percentages.</p>
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10 pages, 4426 KiB  
Article
GTA Weldability of Rolled High-Entropy Alloys Using Various Filler Metals
by Hyunbin Nam, Seonghoon Yoo, Junghoon Lee, Youngsang Na, Nokeun Park and Namhyun Kang
Metals 2020, 10(10), 1371; https://doi.org/10.3390/met10101371 - 14 Oct 2020
Cited by 7 | Viewed by 2719
Abstract
Gas tungsten arc (GTA) weldability of rolled CoCrFeMnNi high-entropy alloys (HEAs) was conducted using stainless steel (STS) 308L and HEA fillers. Microstructure and mechanical properties of the welds were examined to determine GTA weldability of the rolled HEA. The welds had no macro-defects, [...] Read more.
Gas tungsten arc (GTA) weldability of rolled CoCrFeMnNi high-entropy alloys (HEAs) was conducted using stainless steel (STS) 308L and HEA fillers. Microstructure and mechanical properties of the welds were examined to determine GTA weldability of the rolled HEA. The welds had no macro-defects, and component behaviour between base metal (BM) and weld metal (WM) showed significant differences in the weld using the STS 308L filler. Macro-segregation of Fe components was confirmed in the central region in the WM using the STS 308L filler. Because the columnar grain sizes of all the WMs were larger than those of the rolled HEA BM irrespective of the filler metals, the tensile properties of the GTA welds were lower than those of the rolled HEA BM, and the tensile fracture occurred in the centreline of each weld. In particular, the tensile properties of the weld using the STS 308L filler deteriorated more than those of the HEA weld. This was induced by the formation of macro-segregation and severe martensite transformation in the centreline of WM. To enhance the weldability of the rolled HEA, the formation of macro-segregation and coarse grains in the WM of GTA welds must be prevented. Full article
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Graphical abstract

Graphical abstract
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<p>Shape of the gas tungsten arc (GTA) weld cross-sections using various filler metals: (<b>a</b>) stainless steel (STS) 308L and (<b>b</b>) high-entropy alloys (HEA). Red- and blue-dotted lines indicate the location of the quantitative electron probe microanalysis (EPMA) and fusion lines, respectively.</p>
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<p>Component segregation of GTA welds produced using various fillers: (<b>a</b>) STS 308L and (<b>b</b>) HEA.</p>
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<p>Compositional behaviour of GTA welds produced using various fillers: (<b>a</b>) STS 308L and (<b>b</b>) HEA.</p>
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<p>XRD patterns of rolled HEA base metal (BM) and GTA welds using HEA and STS 308L fillers.</p>
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<p>Microstructural behaviour of (<b>a</b>) rolled HEA BM, (<b>b</b>) HAZ, (<b>c</b>–<b>f</b>) near the fusion line and WM centreline using various fillers: (<b>c</b>, <b>e</b>) STS 308L and (<b>d</b>, <b>f</b>) HEA.</p>
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<p>Hardness distribution behaviour of the welds using HEA and STS 308L fillers.</p>
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<p>Tensile properties of rolled HEA BM and welds using HEA and STS 308L fillers tested at 298 K: (<b>a</b>) tensile stress-strain curves and (<b>b</b>) fracture positions in the welds.</p>
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<p>Microstructures near the tensile fracture position tested at 289 K in each weld: (<b>a</b>) using STS 308L filler and (<b>b</b>) HEA filler.</p>
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<p>Microstructures near the tensile fracture position tested at 289 K in each weld using: (<b>a</b>) STS 308L filler and (<b>b</b>) HEA filler.</p>
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