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Search Results (3,952)

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Keywords = wear mechanism

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20 pages, 1639 KiB  
Article
The Influence of Mechanical Properties of Laser-Melted Tungsten Carbide Composite with Nickel/Cobalt Ingredients
by Xiao-Dong Wang and Ming-Der Jean
Materials 2024, 17(22), 5636; https://doi.org/10.3390/ma17225636 (registering DOI) - 18 Nov 2024
Abstract
This study used statistical tools to optimise WC/Co/Ni welds and model construction to improve the mechanical properties of coatings by laser cladding. The effect of the parameters on the wear performance of the weld was determined by analysis of variance. In addition, a [...] Read more.
This study used statistical tools to optimise WC/Co/Ni welds and model construction to improve the mechanical properties of coatings by laser cladding. The effect of the parameters on the wear performance of the weld was determined by analysis of variance. In addition, a polynomial model was constructed using the response surface method based on the experimental data of the orthogonal array designed by Taguchi. The experimental results show that there are white initial precipitation carbides and grey areas of WC mixed with Co and Ni compounds, while less wear and less plastic deformation are observed with WC/Co/Ni alloys. By adding Co/Ni alloys, the composite coating extension is seen to have good anti-wear performance. Based on the regression model, a pairwise interaction model was successfully constructed and further modelling of the 3D contour of the wear behaviour was explored. Comparing all the experiments, the predictions of the interaction model were found to be reliable, with an average error of 8.75%. The findings show that there is a very close match between the predicted values of RSM for wear performance and the experimental data, which proves the effectiveness of the Taguchi design-based RSM in improving the mechanical properties of laser cladding. Full article
18 pages, 2514 KiB  
Article
Aloe Vera as a Printed Coating to Mitigate the Wear of Textiles
by Michail Karypidis, Amalia Stalika, Maria Zarkogianni, Apostolos Korlos and Eleftherios G. Andriotis
Coatings 2024, 14(11), 1467; https://doi.org/10.3390/coatings14111467 - 18 Nov 2024
Abstract
Aloe vera is well known for its biological properties as a bioflavonoid anti-inflammatory and antibacterial agent. It has been used frequently in the food sector as a food coating due to its hygroscopic properties and as an ingredient in the lucrative cosmetic industry. [...] Read more.
Aloe vera is well known for its biological properties as a bioflavonoid anti-inflammatory and antibacterial agent. It has been used frequently in the food sector as a food coating due to its hygroscopic properties and as an ingredient in the lucrative cosmetic industry. Studies have also included aloe vera as an eco-friendly green solution based on these properties. The current research focuses on the use of aloe vera gel in printing pastes as an alternative sustainable solution to synthetic thickeners, evaluating its wet performance and ease of fabric stitching, and has been inspired by studies that similarly used this substance and measured its effect on the fabric’s coefficient of friction and antimicrobial action. In the current study, printing pastes with natural colourants, such as saffron, curcumin, and annatto, and aloe vera gel thickener derived from natural leaves from Crete increased the fabric’s mechanical resistance to abrasion compared to the untreated pastes. The measured performance did not differ substantially from prints with traditional synthetic pastes, hence tolerating the substitution with the non-contaminant variant. The enhanced resistance to abrasion and wear extends the fabric’s serviceable life and resulting garments, decreasing the need for high industry processing volumes and, as a result, reducing pollution. The resistance to wear was evaluated using the dominant method in textile testing of the Martindale apparatus, which measured the cycles to failure, weight loss, and general appearance deterioration using the official photographic standards. Full article
(This article belongs to the Special Issue Coatings for Antimicrobial Textiles)
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<p>Experimental set up of (<b>a</b>) abrasion resistance on Martindale abrasion apparatus, (<b>b</b>) microscope, and (<b>c</b>) test specimen failing point.</p>
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<p>Abrasion resistance cycles to failure for knitted fabric.</p>
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<p>Abrasion resistance cycles to failure for woven fabric.</p>
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<p>Percentage mass loss due to abrasion for knitted fabric.</p>
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<p>Percentage mass loss due to abrasion for woven fabric.</p>
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<p>Surface fuzzing of fabric samples comes at a later stage in the coated samples. (<b>a</b>) Untreated knitted fabric; (<b>b</b>) printed knitted fabric; (<b>c</b>) untreated woven fabric; (<b>d</b>) printed woven fabric.</p>
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<p>Longer fibrils protruding from the surface of the knitted (<b>a</b>) untreated samples compared to (<b>b</b>) aloe-treated pastes coated samples, after 6000 rubbing cycles.</p>
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<p>Abrasion resistance cycles to failure plot of knitted fabric substrates for stepwise statistical analysis.</p>
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<p>Abrasion resistance cycles to failure plot of woven fabric substrates for stepwise statistical analysis.</p>
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<p>The abraded fabric under SEM analysis. (<b>a</b>) Low magnification (<b>b</b>) and high magnification at 5000 cycles.</p>
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14 pages, 49185 KiB  
Article
Investigating Influence of Mo Elements on Friction and Wear Performance of Nickel Alloy Matrix Composites in Air from 25 to 800 °C
by Jinming Zhen, Yunxiang Han, Lin Yuan, Zhengfeng Jia and Ran Zhang
Lubricants 2024, 12(11), 396; https://doi.org/10.3390/lubricants12110396 (registering DOI) - 18 Nov 2024
Abstract
Rapid developments in aerospace and nuclear industries pushed forward the search for high-performance self-lubricating materials with low friction and wear characteristics under severe environment. In this paper, we investigated the influence of the Mo element on the tribological performance of nickel alloy matrix [...] Read more.
Rapid developments in aerospace and nuclear industries pushed forward the search for high-performance self-lubricating materials with low friction and wear characteristics under severe environment. In this paper, we investigated the influence of the Mo element on the tribological performance of nickel alloy matrix composites from room temperature to 800 °C under atmospheric conditions. The results demonstrated that composites exhibited excellent lubricating (with low friction coefficients of 0.19–0.37) and wear resistance properties (with low wear rates of 2.5–28.1 × 10−5 mm3/Nm), especially at a content of elemental Mo of 8 wt. % and 12 wt. %. The presence of soft metal Ag on the sliding surface as solid lubricant resulted in low friction and wear rate in a temperature range from 25 to 400 °C, while at elevated temperatures (600 and 800 °C), the effective lubricant contributed to the formation of a glazed layer rich in NiCr2O4, BaF2/CaF2, and Ag2MoO4. SEM, EDS, and the Raman spectrum indicated that abrasive and fatigue wear were the main wear mechanisms for the studied composites during sliding against the Si3N4 ceramic ball. The obtained results provide an insightful suggestion for future designing and fabricating solid lubricant composites with low friction and wear properties. Full article
(This article belongs to the Special Issue Tribology in Manufacturing Engineering)
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<p>COF vs. testing temperature of nickel alloy matrix composites.</p>
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<p>COF vs. testing temperature of nickel alloy matrix composites.</p>
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<p>Three-dimensional morphologies of worn surface for 0Mo and 5Mo composites: (<b>a</b>) 0Mo 25 °C, (<b>b</b>) 0Mo 400 °C, (<b>c</b>) 0Mo 600 °C, (<b>d</b>) 0Mo 800 °C; (<b>e</b>) 5Mo 25 °C, (<b>f</b>) 5Mo 400 °C, (<b>g</b>) 5Mo 600 °C, (<b>h</b>) 5Mo 800 °C.</p>
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<p>Three-dimensional morphologies of worn surface for 8Mo and 12Mo composites: (<b>a</b>) 8Mo 25 °C, (<b>b</b>) 8Mo 400 °C, (<b>c</b>) 8Mo 600 °C, (<b>d</b>) 8Mo 800 °C; (<b>e</b>) 12Mo 25 °C, (<b>f</b>) 12Mo 400 °C, (<b>g</b>) 12Mo 600 °C, (<b>h</b>) 12Mo 800 °C.</p>
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<p>SEM images of worn surfaces for composites at 25 °C: (<b>a</b>) 0Mo, (<b>b</b>) 5Mo, (<b>c</b>) 12Mo.</p>
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<p>SEM images of worn surfaces for composites at 400 °C: (<b>a</b>) 0Mo, (<b>b</b>) 5Mo, (<b>c</b>) 8Mo.</p>
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<p>SEM images of the worn surfaces for the composites at 600 °C: (<b>a</b>) 0Mo, (<b>b</b>) 5Mo, (<b>c</b>) 8Mo.</p>
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<p>SEM images of the worn surfaces for the composites at 800 °C: (<b>a</b>) 0Mo, (<b>b</b>) 5Mo, (<b>c</b>) 8Mo.</p>
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<p>SEM images of worn scar for Si<sub>3</sub>N<sub>4</sub> ceramic ball: (<b>a</b>) 0Mo 25 °C, (<b>b</b>) 0Mo 400 °C, (<b>c</b>) 0Mo 800 °C, (<b>d</b>) 5Mo 25 °C, (<b>e</b>) 5Mo 400 °C, (<b>f</b>) 5Mo 800 °C.</p>
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<p>SEM images and corresponding EDS mapping of worn surface for Si<sub>3</sub>N<sub>4</sub> ceramic ball sliding against 0Mo composite at 800 °C.</p>
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<p>SEM images and corresponding EDS mapping of worn surface for Si<sub>3</sub>N<sub>4</sub> ceramic ball sliding against 5Mo composite at 800 °C.</p>
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<p>SEM images of worn scar for Si<sub>3</sub>N<sub>4</sub> ceramic ball: (<b>a</b>) 8Mo 25 °C, (<b>b</b>) 8Mo 400 °C, (<b>c</b>) 8Mo 800 °C, (<b>d</b>) 12Mo 800 °C.</p>
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<p>SEM images and corresponding EDS mapping of worn scar for Si<sub>3</sub>N<sub>4</sub> ceramic ball sliding against 8Mo composite at 25 °C.</p>
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<p>SEM images of worn scar for Si<sub>3</sub>N<sub>4</sub> ceramic ball and corresponding EDS mapping coupled with 8Mo composite at 400 °C.</p>
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<p>SEM images and corresponding EDS mapping of worn surface for Si<sub>3</sub>N<sub>4</sub> ceramic ball coupled with 8Mo composite at 800 °C.</p>
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<p>SEM images and corresponding EDS mapping of worn surface for Si<sub>3</sub>N<sub>4</sub> ceramic ball sliding against 12Mo composite at 800 °C.</p>
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<p>SEM images of 8Mo composite and corresponding element distribution at 800 °C.</p>
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<p>SEM images of sliding surface for 12Mo composite and corresponding element distribution at 800 °C.</p>
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<p>Raman spectrum for nickel alloy matrix composite: (<b>a</b>) worn surface for four composites at 800 °C, (<b>b</b>) 12Mo composite at 25, 200, 400, and 600 °C.</p>
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15 pages, 18440 KiB  
Article
Evaluation of Continuous GMA Welding Characteristics Based on the Copper-Plating Method of Solid Wire Surfaces
by Dong-Yoon Kim and Jiyoung Yu
Metals 2024, 14(11), 1300; https://doi.org/10.3390/met14111300 - 18 Nov 2024
Abstract
Gas metal arc welding (GMAW) is widely used in various industries, such as automotive and heavy equipment manufacturing, because of its high productivity and speed, with solid wires being selected based on the mechanical properties required for welded joints. GMAW consists of various [...] Read more.
Gas metal arc welding (GMAW) is widely used in various industries, such as automotive and heavy equipment manufacturing, because of its high productivity and speed, with solid wires being selected based on the mechanical properties required for welded joints. GMAW consists of various components, among which consumables such as the contact tip and continuously fed solid wire have a significant impact on the weld quality. In particular, the copper-plating method can affect the conductivity and arc stability of the solid wire, causing differences in the continuous welding performance. This study evaluated the welding performance during 60 min continuous GMAW using an AWS A5.18 ER70S-3 solid wire, which was copper-plated using chemical plating (C-wire) and electroplating (E-wire). The homogeneity and adhesion of the copper-plated surface of the E-wire were superior to those of the C-wire. The E-wire exhibited better performance in terms of arc stability. The wear rate of the contact tip was approximately 45% higher when using the E-wire for 60 min of welding compared with the C-wire, which was attributed to the larger variation rate in the cast and helix in the E-wire. Additionally, the amount of spatter adhered to the nozzle during 60 min, with the E-wire averaging 5.9 g, approximately half that of the C-wire at 12.9 g. The E-wire exhibits superior arc stability compared with the C-wire based on the spatter amount adhered to the nozzle. This study provides an important reference for understanding the impact of copper plating methods and wire morphology on the replacement cycles of consumable welding parts in automated welding processes such as continuous welding and wire-arc additive manufacturing. Full article
(This article belongs to the Special Issue Welding and Joining of Advanced High-Strength Steels (2nd Edition))
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<p>Appearance and specifications of the welding workability evaluation system.</p>
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<p>Schematic of the welding current and voltage measurement.</p>
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<p>CT results of solid wire contact condition inside the contact tip during wire feeding.</p>
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<p>Surface analysis results of the solid wire according to the plating method; drawing direction: (<b>a</b>) C-wire; (<b>b</b>) E-wire; transverse direction; (<b>c</b>) C-wire; (<b>d</b>) E-wire.</p>
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<p>Analysis of the copper surface homogeneity of the solid wire based on the plating method: (<b>a</b>) C-wire; (<b>b</b>) E-wire.</p>
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<p>Results of coating adhesion: (<b>a</b>) C-wire; (<b>b</b>) E-wire.</p>
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<p>Arc stability evaluation for C-wire during 1 h of welding (average current/voltage and standard deviation): (<b>a</b>) C-wire #1; (<b>b</b>) C-wire #2.</p>
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<p>Actual welding current/voltage waveform of C-wire (10 kHz, 10 s): (<b>a</b>) stable welding section (point a); (<b>b</b>) unstable welding section (point b).</p>
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<p>Analysis of the contact tip and wire after 48.5 min of welding with C-wire #1: (<b>a</b>) the contact tip inside; (<b>b</b>) surface of C-wire after welding.</p>
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<p>Arc stability evaluation for the E-wire during 1 h of welding (average current/voltage and standard deviation): (<b>a</b>) C-wire #1; (<b>b</b>) C-wire #2.</p>
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<p>Weld appearance during continuous welding: (<b>a</b>) C-wire #1; (<b>b</b>) C-wire #2; (<b>c</b>) E-wire #1; (<b>d</b>) E-wire #2.</p>
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<p>Appearance of the contact tip end during continuous welding.</p>
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<p>Nozzle spatter adhesion state by welding time for each solid wire during continuous welding.</p>
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19 pages, 14171 KiB  
Article
Mechanical, Tribological, and Corrosion Resistance Properties of (TiAlxCrNbY)Ny High-Entropy Coatings Synthesized Through Hybrid Reactive Magnetron Sputtering
by Nicolae C. Zoita, Mihaela Dinu, Anca C. Parau, Iulian Pana and Adrian E. Kiss
Crystals 2024, 14(11), 993; https://doi.org/10.3390/cryst14110993 (registering DOI) - 17 Nov 2024
Viewed by 270
Abstract
This study investigates the effects of aluminum and nitrogen content on the microstructure, mechanical properties, and tribological performance of high-entropy coatings based on (TiCrAlxNbY)Ny systems. Using a hybrid magnetron sputtering technique, both metallic and nitride coatings were synthesized and evaluated. [...] Read more.
This study investigates the effects of aluminum and nitrogen content on the microstructure, mechanical properties, and tribological performance of high-entropy coatings based on (TiCrAlxNbY)Ny systems. Using a hybrid magnetron sputtering technique, both metallic and nitride coatings were synthesized and evaluated. Increasing the aluminum concentration led to a transition from a crystalline to a nanocrystalline and nearly amorphous (NC/A) structure, with the TiAl0.5CrNbY sample (11.8% Al) exhibiting the best balance of hardness (6.8 GPa), elastic modulus (87.1 GPa), and coefficient of friction (0.64). The addition of nitrogen further enhanced these properties, transitioning the coatings to a denser fine-grained FCC structure. The HN2 sample (45.8% nitrogen) displayed the highest hardness (21.8 GPa) but increased brittleness, while the HN1 sample (32.9% nitrogen) provided an optimal balance of hardness (14.3 GPa), elastic modulus (127.5 GPa), coefficient of friction (0.60), and wear resistance (21.2 × 10−6 mm3/Nm). Electrochemical impedance spectroscopy revealed improved corrosion resistance for the HN1 sample due to its dense microstructure. Overall, the (TiAl0.5CrNbY)N0.5 coating achieved the best performance for friction applications, such as break and clutch systems, requiring high coefficients of friction, high wear resistance, and durability. Full article
(This article belongs to the Special Issue Advances of High Entropy Alloys)
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<p>2ϴ/ϴ X-ray diffraction patterns corresponding to H1–H4 coatings.</p>
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<p>AFM surface images (3 × 3 µm<sup>2</sup>) corresponding to (<b>a</b>) H1 and (<b>b</b>) H4 samples. Cross-sectional HR-SEM images corresponding to (<b>c</b>) H1 and (<b>d</b>) H4 samples.</p>
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<p>Elemental cross-sectional mapping corresponding to H1 coating, 2.15 × 1.54 μm<sup>2</sup>.</p>
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<p>(<b>a</b>) The averaged values of hardness (H) and Young’s modulus (E). (<b>b</b>) Wear rate. (<b>c</b>) Friction coefficient evolution.</p>
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<p>(<b>a</b>) 2θ/θ X-ray diffraction patterns and (<b>b</b>) XRR experimental (scattered points) and simulated patterns (continuous lines) corresponding to samples H3, HN1, and HN2; (<b>c</b>) average mass density variation with nitrogen content.</p>
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<p>AFM surface images (3 × 3 µm<sup>2</sup>) corresponding to (<b>a</b>) H3, (<b>b</b>) HN1, and (<b>c</b>) HN2 samples. Cross-sectional HR-SEM images corresponding to (<b>d</b>) H3, (<b>e</b>) HN1, and (<b>f</b>) HN2 samples.</p>
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<p>Mechanical and tribological properties of (TiAl<sub>0.5</sub>CrNbY)N<sub>y</sub>/C45 (0 ≤ y ≤ 0.85). (<b>a</b>) Hardness (H) and Young’s modulus (E). (<b>b</b>) Coefficient of friction. (<b>c</b>) Wear rate.</p>
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<p>SEM micrographs of wear tracks after tribological test corresponding to samples (<b>a</b>) H3 (×300), (<b>b</b>) HN1 (×500), and HN2 (×500). Figures (<b>d</b>) and (<b>e</b>) are magnified views (×1000) of (<b>b</b>) and (<b>c</b>), respectively.</p>
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<p>(<b>a</b>) Nyquist, (<b>b</b>) Bode magnitude, and (<b>c</b>) phase diagrams.</p>
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32 pages, 16212 KiB  
Article
Modeling and Monitoring of the Tool Temperature During Continuous and Interrupted Turning with Cutting Fluid
by Hui Liu, Markus Meurer and Thomas Bergs
Metals 2024, 14(11), 1292; https://doi.org/10.3390/met14111292 - 15 Nov 2024
Viewed by 294
Abstract
In metal cutting, a large amount of mechanical energy converts into heat, leading to a rapid temperature rise. Excessive heat accelerates tool wear, shortens tool life, and hinders chip breakage. Most existing thermal studies have focused on dry machining, with limited research on [...] Read more.
In metal cutting, a large amount of mechanical energy converts into heat, leading to a rapid temperature rise. Excessive heat accelerates tool wear, shortens tool life, and hinders chip breakage. Most existing thermal studies have focused on dry machining, with limited research on the effects of cutting fluids. This study addresses that gap by investigating the thermal behavior of cutting tools during continuous and interrupted turning with cutting fluid. Tool temperatures were first measured experimentally by embedding a thermocouple in a defined position within the tool. These experimental results were then combined with simulations to evaluate temperature changes, heat partition, and cooling efficiency under various cutting conditions. This work presents novel analytical and numerical models. Both models accurately predicted the temperature distribution, with the analytical model offering a computationally more efficient solution for industrial use. Experimental results showed that tool temperature increased with cutting speed, feed, and cutting depth, but the heat partition into the tool decreased. In continuous cutting, cooling efficiency was mainly influenced by feed rate and cutting depth, while cutting speed had minimal impact. Interrupted cutting improved cooling efficiency, as the absence of chips and workpieces during non-cutting phases allowed the cutting fluid to flow over the tool surface at higher speeds. The convective cooling coefficient was determined through inverse calibration. A comparative analysis of the analytical and numerical simulations revealed that the analytical model can underestimate the temperature distribution for complex tool structures, particularly non-orthogonal hexahedral geometries. However, the relative error remained consistent across different cutting conditions, with less error observed in interrupted cutting compared to continuous cutting. These findings highlight the potential of analytical models for optimizing thermal management in metal turning processes. Full article
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<p>Temperature measuring hole and installation position of the sensors.</p>
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<p>Experimental setup for measuring the tool temperature during turning under cutting fluid conditions.</p>
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<p>Microstructure, mechanical properties, and chemical composition of AISI 1045 workpiece.</p>
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<p>AISI 1045 specimen for interrupted turning according to VDI 3324.</p>
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<p>Setup of the heat source and boundary conditions of the numerical temperature model.</p>
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<p>Setup of the heat source and boundary conditions of the analytcial temperature model.</p>
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<p>Process force components measured during continuous turning with and without cutting fluid.</p>
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<p>Tool–chip contact thickness and contact area measured using an optical microscope.</p>
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<p>Chip shapes under different cutting conditions during continuous dry turning.</p>
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<p>Simulated and measured tool temperature for continuous dry turning.</p>
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<p>Heat partition into the tool for continuous turning without cutting fluid.</p>
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<p>Chip shapes under different cutting conditions during continuous turning with cutting fluid (<math display="inline"><semantics> <msub> <mi>p</mi> <mrow> <mi>c</mi> <mi>f</mi> </mrow> </msub> </semantics></math> = 80 bar).</p>
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<p>Simulated and measured tool temperature for continuous turning with cutting fluid (<math display="inline"><semantics> <msub> <mi>p</mi> <mrow> <mi>c</mi> <mi>f</mi> </mrow> </msub> </semantics></math> = 80 bar).</p>
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<p>Comparison of the convective cooling coefficient of the tool rake face for continuous turning, determined by the tool temperature using the numerical and analytical models.</p>
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<p>Tool rake face temperature at <math display="inline"><semantics> <msub> <mi>a</mi> <mi>p</mi> </msub> </semantics></math> = 2.5 mm, continuous turning with cutting fluid.</p>
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<p>Process force components measured during interrupted turning with and without cutting fluid.</p>
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<p>Example of the temperature development from measurement and simulation, and heat input into the tool for the simulation. (<math display="inline"><semantics> <msub> <mi>v</mi> <mi>c</mi> </msub> </semantics></math> = 70 m/min, <math display="inline"><semantics> <msub> <mi>a</mi> <mi>p</mi> </msub> </semantics></math> = 2.5 mm, <span class="html-italic">f</span> = 0.3 mm).</p>
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<p>Temperature fluctuations from measurement and simulation for interrupted turning without cutting fluid.</p>
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<p>Heat partition into the tool for interrupted turning without cutting fluid.</p>
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<p>Temperature fluctuations from measurement and simulation for interrupted turning with cutting fluid (<math display="inline"><semantics> <msub> <mi>p</mi> <mrow> <mi>c</mi> <mi>f</mi> </mrow> </msub> </semantics></math> = 10 bar).</p>
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<p>Convective cooling coefficient of the tool rake face for interrupted turning, determined by the tool temperature using the numerical model.</p>
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<p>Tool rake face temperature at <math display="inline"><semantics> <msub> <mi>a</mi> <mi>p</mi> </msub> </semantics></math> = 0.8 mm, continuous turning without cutting fluid.</p>
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<p>Tool rake face temperature at <math display="inline"><semantics> <msub> <mi>a</mi> <mi>p</mi> </msub> </semantics></math> = 2.5 mm, continuous turning without cutting fluid.</p>
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<p>Tool rake face temperature at <math display="inline"><semantics> <msub> <mi>a</mi> <mi>p</mi> </msub> </semantics></math> = 0.8 mm, continuous turning with cutting fluid.</p>
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<p>Chip shapes during interrupted turning with and without cutting fluid.</p>
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18 pages, 7690 KiB  
Article
A Comparison of the Microstructure and Mechanical Properties of RSW and RFSSW Joints in AA6061-T4 for Automotive Applications
by Damon Gale, Taylor Smith, Yuri Hovanski, Kate Namola and Jeremy Coyne
J. Manuf. Mater. Process. 2024, 8(6), 260; https://doi.org/10.3390/jmmp8060260 - 14 Nov 2024
Viewed by 483
Abstract
To reduce vehicle weight and improve energy efficiency, automotive manufacturers are increasingly using aluminum body panels. However, the traditional joining method, Resistance Spot Welding (RSW), presents challenges like weld porosity and electrode degradation when used with aluminum. These issues have driven the industry [...] Read more.
To reduce vehicle weight and improve energy efficiency, automotive manufacturers are increasingly using aluminum body panels. However, the traditional joining method, Resistance Spot Welding (RSW), presents challenges like weld porosity and electrode degradation when used with aluminum. These issues have driven the industry to explore alternative, more effective methods for joining aluminum in vehicle manufacturing such as Refill Friction Stir Spot Welding (RFSSW). This research reports on a comparison of the microstructure and mechanical properties of welds made with RSW and RFSSW in AA6061-T4 automotive sheets. This comparison includes CT scanning, optical and SEM imaging, statistical microscopy, hardness testing, tensile testing, and fatigue testing. The results showed that RFSSW produced fully consolidated welds with a refined, equiaxed grain structure that outperformed RSW’s dendritic grain structure by as much as 73% in tensile testing and 2600% in fatigue testing. These results suggest that future designs utilizing RFSSW could incorporate fewer joints, reducing processing time, energy consumption, and tool wear. Cost studies also found that RFSSW consumes 2.5% of the energy that RSW does per joint, demonstrating that RFSSW is positioned as the preferred method for joining aluminum automotive sheets. Full article
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<p>The RSW process.</p>
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<p>The four stages of RFSSW: (<b>A</b>) clamping, (<b>B</b>) plunging, (<b>C</b>) refilling, and (<b>D</b>) lifting.</p>
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<p>(<b>A</b>) Drawing of the test coupon’s width, height, and weld placement in (<b>B</b>) 2 sheet stack-ups and (<b>C</b>) 3 sheet stack-ups.</p>
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<p>Surface profiles of RFSSW and RSW.</p>
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<p>CT Scan images of 2.0 mm/2.5 mm/1.2 mm stack-up utilizing: (<b>A</b>) RFSSW, (<b>B</b>) RSW.</p>
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<p>(<b>A</b>) Locations of EBSD scans for RFSSW (<b>Top</b>) and RSW (<b>Bottom</b>); (<b>B</b>) Grain maps of RFSSW (<b>Left</b>) and RSW (<b>Right</b>) at 1000× magnification; (<b>C</b>) Grain size distribution of RFSSW (I. nugget center and II. Nugget edge) and RSW (III. Nugget center and IV. Nugget edge).</p>
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<p>Microhardness heat maps of RFFSW and RSW welds (Vickers).</p>
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<p>(<b>A</b>) Fracture modes (nugget pullout and interfacial fracture); (<b>B</b>) Difference in tensile strength between RFSSW and RSW.</p>
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<p>(<b>A</b>) Elongation at UTS for RFSSW and RSW; (<b>B</b>) SEM images at 2500× magnification of the fracture surfaces, RFSSW (ductile dimple) and RSW (brittle fraction).</p>
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<p>Fatigue life curves of RFSSW and RSW.</p>
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15 pages, 5813 KiB  
Article
Effect of Pressure on the Microstructure and Wear Performance of Cr-Mn-Mo Alloyed Steel Prepared by Squeeze Casting
by Yuan Zhuang, Yujiang Hao, Lei Guo and Xinhao Wu
Lubricants 2024, 12(11), 392; https://doi.org/10.3390/lubricants12110392 - 14 Nov 2024
Viewed by 321
Abstract
In this study, the effects of applied pressure (0, 90, 120, and 150 MPa) during solidification on the microstructure, mechanical properties, and impact–abrasive wear resistance of Cr-Mn-Mo steel prepared by squeeze casting were systematically investigated. The results demonstrated that the materials produced under [...] Read more.
In this study, the effects of applied pressure (0, 90, 120, and 150 MPa) during solidification on the microstructure, mechanical properties, and impact–abrasive wear resistance of Cr-Mn-Mo steel prepared by squeeze casting were systematically investigated. The results demonstrated that the materials produced under pressure showed smaller grains compared to those of the samples fabricated without pressure. Compared to the unpressurized sample, the grain diameter of the sample prepared at 120 MPa decreased by 37.7%, the length of the primary arm shortened by 40.7%, and the spacing of the secondary arm contracted by 14.1%. Furthermore, the impact toughness results indicated that the samples prepared without pressure exhibited brittle fracture characteristics, whereas quasi-destructive fractures predominated in the samples prepared at 120 MPa. Simultaneously, three-point bending strength exhibited a gradual increase with increasing pressure, reaching a maximum value of 855.5 MPa when prepared under 150 MPa. Additionally, the impact–abrasive wear resistance of Cr-Mn-Mo alloyed steel produced by squeeze casting was significantly enhanced compared to the samples produced without pressure. The samples without external pressure exhibited a combination of abrasive and adhesive wear, whereas the wear characteristics of the samples prepared under pressure includes grooves, cutting marks, flaking pits, and accumulating ridges. Full article
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<p>Schematic diagram for the preparation of the liner by squeeze casting.</p>
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<p>Measurement of SDAS size by the cutting line method.</p>
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<p>(<b>a</b>) Schematic diagram of the impact–abrasive wear tests; (<b>b</b>) Size of wear sample and counterpart ring.</p>
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<p>(<b>a</b>–<b>d</b>) Microstructure of the samples prepared under 0 MPa, 90 MPa, 120 MPa, and 150 MPa at lower magnification; (<b>b′</b>–<b>d′</b>) Microstructure of the samples prepared under 90 MPa, 120 MPa, and 150 MPa at higher magnification.</p>
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<p>(<b>a</b>) XRD analysis results of the sample prepared at 90 MPa; (<b>b</b>) Comparison of the martensite diameter of samples prepared at various pressures.</p>
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<p>Mechanical properties including hardness, impact toughness, and bending strength of the samples prepared at various pressures.</p>
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<p>Fracture morphology of the prepared samples: (<b>a</b>) prepared under 0 MPa; (<b>b</b>) prepared under 120 MPa.</p>
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<p>(<b>a</b>) Relationship between the worn time and wear weight loss of the steels produced at various pressures; (<b>b</b>) Average worn rate of the steels fabricated at various pressures.</p>
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<p>The worn morphology of the steels prepared under various pressures: (<b>a</b>,<b>a′</b>) 0 MPa; (<b>b</b>,<b>b′</b>) 90 MPa; (<b>c</b>,<b>c′</b>) 120 MPa; (<b>d</b>,<b>d′</b>) 150 MPa.</p>
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<p>EDS results of Point A (<b>a</b>) and Point B (<b>b</b>) in <a href="#lubricants-12-00392-f009" class="html-fig">Figure 9</a>b′.</p>
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<p>Schematic illustration of the wear mechanisms of the samples: (<b>a</b>) the formation of cutting and grooves; (<b>b</b>) the formation of ridges; (<b>c</b>) the formation of spalling pits; (<b>d</b>) the formation of inserted abrasive particles.</p>
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20 pages, 8912 KiB  
Article
Test Results and Considerations for Design Improvements of L-CADEL v.3 Elbow-Assisting Device
by Marco Ceccarelli, Sergei Kotov, Earnest Ofonaike and Matteo Russo
Machines 2024, 12(11), 808; https://doi.org/10.3390/machines12110808 - 14 Nov 2024
Viewed by 227
Abstract
The elbow-assisting device, L-CADEL, was analyzed by testing a prototype of design version three (v3) with the aim of discussing design improvements to solve problems and improve operational performance. The test results reported are from a lab testing campaign with 15 student volunteers [...] Read more.
The elbow-assisting device, L-CADEL, was analyzed by testing a prototype of design version three (v3) with the aim of discussing design improvements to solve problems and improve operational performance. The test results reported are from a lab testing campaign with 15 student volunteers from the engineering and physiotherapy disciplines. The main aspects of attention of the reported investigation are data analyses for motion diagnostics, comfort in wearing, operation efficiency, and the mechanical design of the arm platform and cable tensioning. Full article
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<p>The main requirements for design issues in a motion-assisting device for the elbow.</p>
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<p>Design of L-CADEL v.3 prototype: (<b>a</b>) conceptual design and (<b>b</b>) prototype installed on a user’s arm.</p>
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<p>Design of L-CADEL v.3 prototype: (<b>a</b>) block diagram and (<b>b</b>) electric circuit design.</p>
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<p>Arm ring platform of L-CADEL v.3 prototype: (<b>a</b>) a CAD model and (<b>b</b>) the built prototype installed on a user’s arm. (1 is the button for changing the motor’s rotation).</p>
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<p>Arm ring platform of L-CADEL v.3 prototype: (<b>a</b>) Conceptual design and (<b>b</b>) electric circuit design.</p>
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<p>Wrist ring platform of L-CADEL v.3 prototype: (<b>a</b>) a CAD model with sizes in mm and (<b>b</b>) the built prototype installed on a user’s wrist. (1 is an IMU sensor; 2 is a cable connection hook).</p>
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<p>EMG sensor of L-CADEL v.3 prototype: (<b>a</b>) EMG electrodes installed on the arm and (<b>b</b>) electric circuit design.</p>
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<p>The third platform for control unit and acquisition and elaboration data of L-CADEL v.3 prototype: (<b>a</b>) block diagram and (<b>b</b>) electric circuit design.</p>
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<p>Testing layout with L-CADEL v.3 prototype: (<b>a</b>) conceptual design and (<b>b</b>) a lab setup.</p>
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<p>A snapshot of a test with the L-CADEL.v3 prototype setup. (<b>a</b>) Starting configuration; (<b>b</b>) intermediate configuiration; (<b>c</b>) final arm flexed configuration.</p>
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<p>Acquired data during a test with L-CADEL.v3 prototype, as in <a href="#machines-12-00808-f010" class="html-fig">Figure 10</a>, in terms of the acceleration components Ax, Ay, Az, and module.</p>
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<p>Acquired data during a test with L-CADEL.v3 prototype, as in <a href="#machines-12-00808-f010" class="html-fig">Figure 10</a>, in terms of the pitch, roll, and yaw angles.</p>
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<p>Acquired data during a test with L-CADEL.v3 prototype, as in <a href="#machines-12-00808-f010" class="html-fig">Figure 10</a>, in terms of power consumption.</p>
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<p>Acquired data during a test with L-CADEL.v3 prototype, as in <a href="#machines-12-00808-f010" class="html-fig">Figure 10</a>, in terms of the EMG response.</p>
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<p>Schemes with aspects of attention for a new L-CADEL v.4 prototype: (<b>a</b>) arm ring platform and (<b>b</b>) wrist ring platform.</p>
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11 pages, 1160 KiB  
Article
Evaluation and Comparison of Manual and Mechanical Endodontic Instrumentation Completed by Undergraduate Dental Students on Endodontic Blocks
by António Ginjeira, Abayomi O. Baruwa and Karla Baumotte
Dent. J. 2024, 12(11), 363; https://doi.org/10.3390/dj12110363 - 14 Nov 2024
Viewed by 459
Abstract
Background: The shaping of root canal space was completed using manual stainless steel files in earlier decades and with the advent of mechanical nickel–titanium (NiTi) instruments, there is potential for more efficient root canal preparation. Despite the advantages of NiTi instruments, their adoption [...] Read more.
Background: The shaping of root canal space was completed using manual stainless steel files in earlier decades and with the advent of mechanical nickel–titanium (NiTi) instruments, there is potential for more efficient root canal preparation. Despite the advantages of NiTi instruments, their adoption in undergraduate dental education remains limited. The aim of this study was to evaluate three root canal instrumentation techniques, manual instrumentation using stainless steel hand files, continuous rotation employing ProTaper Gold (PTG) files, and reciprocation with WaveOne Gold (WOG) files, on endodontic resin blocks to assess the quality of preparation and the time required for instrumentation. Methods: A total of 36 third-year dental students, all lacking prior experience in root canal procedures, were divided into six groups to prepare 108 resin endodontic blocks with each student preparing 3 blocks. Images were captured at the preoperative, intraoperative, and postoperative stages to facilitate comparisons and measurements of the prepared blocks to assess the degree of resin removal, apical deviation, and mid-cervical wear. Furthermore, questionnaires were distributed to assess the students’ experiences and satisfaction with the techniques. The Friedman test, Wilcoxon test with Bonferroni correction, and Kruskal–Wallis test with Mann–Whitney U test were used to analyse and compare techniques, with the level of significance set at p < 0.05. Results: Instrumentation with PTG exhibited significantly reduced apical deviation (0.073 ± 0.003) compared to both the WOG and manual instrumentations (p < 0.001). Significant differences in mid-cervical wear were observed only between PTG and the manual instrumentation. In terms of resin removal, the manual instrumentation displayed greater variability and was five times slower to complete the instrumentation. In total, 90% of students favoured mechanical instrumentation, with substantial preferences for them over manual techniques. Conclusions: Mechanical instrumentation techniques, notably with the PTG system, were significantly faster and more effective in preparation quality. This highlights the potential for the inclusion of mechanical instrumentation in undergraduate dental curricula. Full article
(This article belongs to the Special Issue Dental Education: Innovation and Challenge)
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<p>(<b>A</b>) Image capturing and reproduction table, (<b>B</b>) grid overlay, and (<b>C</b>) measuring points 1, 2, 3, and 4.</p>
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<p>(<b>A</b>) Points registrations marked 1–4 for adequate alignment of images (in green is source point in image 1 and red is destination point in image 2 and (<b>B</b>) the overlay and comparison of images.</p>
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26 pages, 14835 KiB  
Article
Mechanical and Tribological Properties of (AlCrNbSiTiMo)N High-Entropy Alloy Films Prepared Using Single Multiple-Element Powder Hot-Pressed Sintered Target and Their Practical Application in Nickel-Based Alloy Milling
by Jeng-Haur Horng, Wen-Hsien Kao, Wei-Chen Lin and Ren-Hao Chang
Lubricants 2024, 12(11), 391; https://doi.org/10.3390/lubricants12110391 - 14 Nov 2024
Viewed by 398
Abstract
(AlCrNbSiTiMo)N high-entropy alloy films with different nitrogen contents were deposited on tungsten carbide substrates using a radio-frequency magnetron sputtering system. Two different types of targets were used in the sputtering process: a hot-pressing sintered AlCrNbSiTi target fabricated using a single powder containing multiple [...] Read more.
(AlCrNbSiTiMo)N high-entropy alloy films with different nitrogen contents were deposited on tungsten carbide substrates using a radio-frequency magnetron sputtering system. Two different types of targets were used in the sputtering process: a hot-pressing sintered AlCrNbSiTi target fabricated using a single powder containing multiple elements and a vacuum arc melting Mo target. The deposited films were denoted as RN0, RN33, RN43, RN50, and RN56, where RN indicates the nitrogen flow ratio relative to the total nitrogen and argon flow rate (RN = (N2/(N2 + Ar)) × 100%). The as-sputtered films were vacuum annealed, with the resulting films denoted as HRN0, HRN33, HRN43, HRN50, and HRN56, respectively. The effects of the nitrogen content on the composition, microstructure, mechanical properties, and tribological properties of the films, in both as-sputtered and annealed states, underwent thorough analysis. The RN0 and RN33 films displayed non-crystalline structures. However, with an increase in nitrogen content, the RN43, RN50, and RN56 films transitioned to FCC structures. Among the as-deposited films, the RN43 film exhibited the best mechanical and tribological properties. All of the annealed films, except for the HRN0 film, displayed an FCC structure. In addition, they all formed an MoO3 solid lubricating phase, which reduced the coefficient of friction and improved the anti-wear performance. The heat treatment HRN43 film displayed the supreme hardness, H/E ratio, and adhesion strength. It also demonstrated excellent thermal stability and the best wear resistance. As a result, in milling tests on Inconel 718, the RN43-coated tool demonstrated a significantly lower flank wear and notch wear, indicating an improved machining performance and extended tool life. Thus, the application of the RN43 film in aerospace manufacturing can effectively reduce the tool replacement cost. Full article
(This article belongs to the Special Issue Recent Advances in Tribological Properties of Machine Tools)
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<p>(<b>a</b>) Diagrammatic sketch of sputtering target configuration, and (<b>b</b>) diagrammatic sketch of film design.</p>
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<p>Morphology and elemental composition of new AlCrNbSiTi powder for hot-pressing sintering targets.</p>
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<p>Schematic showing tool wear and notch wear measurement positions.</p>
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<p>Element content of (<b>a</b>) as-sputtered and (<b>b</b>) heat-treated (AlCrNbSiTiMo)N films.</p>
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<p>X-ray diffraction patterns of (<b>a</b>) as-sputtered and (<b>b</b>) heat-treated (AlCrNbSiTiMo)N films.</p>
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<p>Cross-section SEM graphics of (AlCrNbSiTiMo)N films: (<b>a</b>) R<sub>N0</sub>, (<b>b</b>) HR<sub>N0</sub>, (<b>c</b>) R<sub>N33</sub>, (<b>d</b>) HR<sub>N33</sub>, (<b>e</b>) R<sub>N43</sub>, (<b>f</b>) HR<sub>N43</sub>, (<b>g</b>) R<sub>N50</sub>, (<b>h</b>) HR<sub>N50</sub>, (<b>i</b>) R<sub>N56</sub>, and (<b>j</b>) HR<sub>N56</sub>.</p>
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<p>SEM surface graphics of (AlCrNbSiTiMo)N films: (<b>a</b>) R<sub>N0</sub>, (<b>b</b>) HR<sub>N0</sub>, (<b>c</b>) R<sub>N33</sub>, (<b>d</b>) HR<sub>N33</sub>, (<b>e</b>) R<sub>N43</sub>, (<b>f</b>) HR<sub>N43</sub>, (<b>g</b>) R<sub>N50</sub>, (<b>h</b>) HR<sub>N50</sub>, (<b>i</b>) R<sub>N56</sub>, and (<b>j</b>) HR<sub>N56</sub>.</p>
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<p>OM graphics of scratch track on R<sub>N33</sub> film.</p>
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<p>Curves of COF for (<b>a</b>) as-deposited (AlCrNbSiTiMo)N films and substrate (WC), and (<b>b</b>) annealed (AlCrNbSiTiMo)N films and substrate (WC).</p>
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<p>SEM graphics and EDS results of worn traces on (<b>a</b>) R<sub>N0</sub> and (<b>b</b>) R<sub>N43</sub> films and (<b>c</b>) R<sub>N43</sub> film enlarged image and (Note: For comparative analysis, the originally existed elemental compositions of the R<sub>N0</sub>, R<sub>N43</sub> films are also shown).</p>
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<p>SEM graphics and EDS results for worn traces on (<b>a</b>) HR<sub>N0</sub> film, (<b>b</b>) HR<sub>N43</sub> film (regular magnification), and (<b>c</b>) HR<sub>N43</sub> film (high magnification). (Note: For comparative analysis, the originally existed elemental compositions of the HR<sub>N0</sub> and HR<sub>N43</sub> films are also provided).</p>
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<p>OM graphics showing the flank wear and notch wear on (<b>a</b>) bare WC cutting tool and (<b>b</b>) R<sub>N43</sub> coated WC cutting tool completing a total processing distance of 18 m.</p>
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<p>(<b>a</b>) Flank wear and (<b>b</b>) Notch wear of bare WC cutting tool and R<sub>N43</sub> coated WC cutting tool compared with other coated tools after completing three processing distances of 6, 12, and 18 m, individually.</p>
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14 pages, 10340 KiB  
Article
Increasing the Wear Resistance of CrWMn Tool Steel Surfaces by Plasma Electrolytic Nitriding and Polishing
by Sergey N. Grigoriev, Tatiana L. Mukhacheva, Ivan V. Tambovskiy, Irina A. Kusmanova, Tatiana M. Golubeva, Pavel A. Podrabinnik, Roman S. Khmyrov, Igor V. Suminov and Sergei A. Kusmanov
Appl. Sci. 2024, 14(22), 10488; https://doi.org/10.3390/app142210488 - 14 Nov 2024
Viewed by 274
Abstract
The positive effect of plasma electrolytic treatment on CrWMn tool steel to increase the wear resistance of its surface is shown. The effect of plasma electrolytic nitriding and subsequent polishing on the structure, phase and elemental composition, microhardness of the surface layer, and [...] Read more.
The positive effect of plasma electrolytic treatment on CrWMn tool steel to increase the wear resistance of its surface is shown. The effect of plasma electrolytic nitriding and subsequent polishing on the structure, phase and elemental composition, microhardness of the surface layer, and surface morphology is established. Steel nitriding leads to the formation of a modified surface layer including Fe2–3N iron nitride and nitrogen martensite, below which hardening martensite is formed, reaching a microhardness value of 1200 HV. Subsequent polishing leads to a decrease in surface roughness by 42–68%. Tribological tests were carried out according to the shaft-bushing scheme. A decrease in the friction coefficient and weight wear of up to 2.6 and 30.1 times, respectively, is shown. The formed structure of the surface layer compensates for the effect of the counter body and determines the destruction of friction bonds by plastic displacement. The wear mechanism has been established and is defined as fatigue wear under dry friction and plastic contact. Full article
(This article belongs to the Section Materials Science and Engineering)
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<p>PEN and PEP installation scheme: 1—ventilation duct; 2—protective screen of the working chamber; 3—linear drive; 4—workpiece-electrode (anode); 5—cylindrical cell-electrode (cathode); 6—working chamber; 7—valve with electric drive; 8—flow meter; 9—heat exchanger; 10—pump; 11—water filter.</p>
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<p>Friction scheme and unit: 1—cylindrical sample; 2—counter body; 3, 4—shaft; 5—crank; 6—pneumatic cylinder; 7—guides; 8—table; 9—strain gauges.</p>
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<p>X-ray diffraction pattern of the CrWMn steel surface after various types of treatment: (<b>a</b>) PEN; (<b>b</b>) PEN and PEP in a solution of NH<sub>4</sub>Cl and C<sub>3</sub>H<sub>8</sub>O<sub>3</sub> for 1 min; (<b>c</b>) PEN and PEP in a solution of NH<sub>4</sub>Cl and C<sub>3</sub>H<sub>8</sub>O<sub>3</sub> for and 2 min; (<b>d</b>) PEN and PEP in (NH<sub>4</sub>)<sub>2</sub>SO<sub>4</sub> solution for 1 min; (<b>e</b>) PEN and PEP in (NH<sub>4</sub>)<sub>2</sub>SO<sub>4</sub> solution for 2 min.</p>
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<p>SEM image of the cross-section of the surface layer of CrWMn steel after various types of treatment: (<b>a</b>) PEN; (<b>b</b>) PEN and PEP in a solution of NH<sub>4</sub>Cl and C<sub>3</sub>H<sub>8</sub>O<sub>3</sub> for 1 min; (<b>c</b>) PEN and PEP in a solution of NH<sub>4</sub>Cl and C<sub>3</sub>H<sub>8</sub>O<sub>3</sub> for 2 min; (<b>d</b>) PEN and PEP in (NH<sub>4</sub>)<sub>2</sub>SO<sub>4</sub> solution for 1 min; (<b>e</b>) PEN and PEP in (NH<sub>4</sub>)<sub>2</sub>SO<sub>4</sub> solution for 2 min.</p>
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<p>Nitrogen concentration distribution in the surface layer of CrWMn steel after various types of treatment. ChG—the solutions of ammonium chloride and glycerol, S—the solutions of ammonium sulfate.</p>
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<p>Data from EDX analysis of the cross-section of CrWMn steel sample after PEN.</p>
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<p>Microstructure of the cross-section of the CrWMn steel surface after PEN: 1—outer layer with inclusions of iron nitrides and residual austenite, 2—martensitic structure with inclusions of iron carbides.</p>
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<p>Microhardness distribution in the surface layer of CrWMn steel after various types of treatment. ChG—the solutions of ammonium chloride and glycerol, S—the solutions of ammonium sulfate.</p>
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<p>Morphology of the CrWMn steel surface after various types of treatment: (<b>a</b>) Untreated; (<b>b</b>) PEN; (<b>c</b>) PEN and PEP in a solution of NH<sub>4</sub>Cl and C<sub>3</sub>H<sub>8</sub>O<sub>3</sub> for 1 min; (<b>d</b>) PEN and PEP in a solution of NH<sub>4</sub>Cl and C<sub>3</sub>H<sub>8</sub>O<sub>3</sub> for 2 min; (<b>e</b>) PEN and PEP in (NH<sub>4</sub>)<sub>2</sub>SO<sub>4</sub> solution for 1 min; (<b>f</b>) PEN and PEP in (NH<sub>4</sub>)<sub>2</sub>SO<sub>4</sub> solution for 2 min.</p>
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<p>Dependence of the friction coefficient of samples made of CrWMn steel after various types of treatment. ChG—the solutions of ammonium chloride and glycerol, S—the solutions of ammonium sulfate.</p>
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<p>Morphology of friction tracks on the CrWMn steel surface after various types of treatment: (<b>a</b>) Untreated; (<b>b</b>) PEN; (<b>c</b>) PEN and PEP in a solution of NH<sub>4</sub>Cl and C<sub>3</sub>H<sub>8</sub>O<sub>3</sub> for 1 min; (<b>d</b>) PEN and PEP in a solution of NH<sub>4</sub>Cl and C<sub>3</sub>H<sub>8</sub>O<sub>3</sub> for 2 min; (<b>e</b>) PEN and PEP in (NH<sub>4</sub>)<sub>2</sub>SO<sub>4</sub> solution for 1 min; (<b>f</b>) PEN and PEP in (NH<sub>4</sub>)<sub>2</sub>SO<sub>4</sub> solution for 2 min.</p>
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15 pages, 6365 KiB  
Article
Finite Element Combined Design and Material Optimization Addressing the Wear in Removable Implant Prosthodontics
by Pejman Shayanfard, Xingchen Tan, Matthias Karl and Frank Wendler
J. Funct. Biomater. 2024, 15(11), 344; https://doi.org/10.3390/jfb15110344 - 14 Nov 2024
Viewed by 337
Abstract
Wear at the male–female interface of retentive elements in implant-supported removable prostheses is the most frequent complication in such applications. The lack of an ideal/optimal insertion path, as well as the fabrication inaccuracies, are the primary contributors to this issue. A male attachment [...] Read more.
Wear at the male–female interface of retentive elements in implant-supported removable prostheses is the most frequent complication in such applications. The lack of an ideal/optimal insertion path, as well as the fabrication inaccuracies, are the primary contributors to this issue. A male attachment with a common ball anchor enhanced by lateral flexibility was investigated as a solution, compared to the widely used rigid ball anchor design. A parametric finite element analysis was performed to compare the wear-inducing maximum strain at the female polymer counterpart by various attachment designs made from titanium and Nitinol. The evolution of mechanical strains causing wear in the female part, as well as the contribution of stresses and martensitic transformation in the implant’s flexible shaft, were evaluated under several insertion misfit scenarios. Results indicate that introducing a long flexible shaft in the titanium implant reduced maximum strains in the female attachment part by up to 61% as compared to the solid ball anchor. Further improvement was observed by using the shape memory alloy Nitinol as shaft material, leading to a minor reduction in stress and strain at the contact surface but allowing for a shorter abutment. Finally, the optimized Nitinol implant design with a short, necked flexible shaft promoting martensitic transformation at low plateau stress resulted in an approximate 90% reduction in maximum strains at the inner surface of the female part during manual insertion, which indicates a significantly reduced wear phenomenon at the contact. Full article
(This article belongs to the Special Issue Biomaterials and Biomechanics Modelling in Dental Implantology)
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<p>Panoramic radiograph of a geriatric patient presenting multiple single-piece implants in the maxilla with balls for prosthesis retention (implant placement alio loco several years ago). Please note that a common path of insertion has not been established for the maxillary implants. The mandibular dentition is failing, but the patient still wanted to postpone treatment.</p>
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<p>Maxillary removable prosthesis not covering the palate as per the patient’s request. New O-rings have been placed inside corresponding metal housings to fit onto the implants. Two O-rings were intentionally removed as the patient was unable to remove the restoration when all six balls were engaged.</p>
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<p>Eight months after prosthesis delivery, the patient complained about loss of retention of her restoration, presenting with the O-rings shown in the bottom line (top line: new O-rings for comparison). Unilateral deterioration of the O-rings following compression of the material during repeated insertion and removal of the prosthesis is obvious.</p>
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<p>(<b>a</b>) Reference: solid Ti implant; (<b>b</b>) Ti and Nitinol implants, where a flexible long shaft is embedded; (<b>c</b>) short Nitinol implant, where the embedded long shaft is 3 mm shorter; (<b>d</b>) short-necked Nitinol implant; (<b>e</b>) representation of a design fault zone denoted as LPZ within the manuscript; and (<b>f</b>) representation of the optimized design in LPZ for the short-necked Nitinol implant.</p>
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<p>Three-dimensional model of a simplistic one-piece attachment with a ball anchor on top for retaining a removable prosthesis; (<b>a</b>) a 3D model of the female part fitting the ball anchor in different views; and (<b>b</b>) representation of the entire assembled FEM model including the surrounding Ti abutment: 1—female part; 2—male attachment part; and 3—Ti implant.</p>
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<p>Misfit types considered in this study: (<b>a</b>) perfect fit; (<b>b</b>) horizontal misfit between male and female attachment parts of 0.2 mm; (<b>c</b>) angulation misfit with the female part rotated (<math display="inline"><semantics> <mrow> <mi>θ</mi> <mo>=</mo> </mrow> </semantics></math> 3 degrees); and (<b>d</b>) horizontal and angulation misfit.</p>
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<p>FEM results for the reference solid Ti implant design. Stresses are depicted as equivalent to von Mises stress, while strains represent maximum principal strain; (<b>a1</b>–<b>a4</b>) perfect fit (see <a href="#jfb-15-00344-f006" class="html-fig">Figure 6</a>a), where the longitudinal axis of the female component aligns with that of the inserted implant; (<b>b1</b>–<b>b4</b>) horizontal misfit: the abutment shifts horizontally for 0.2 mm (see <a href="#jfb-15-00344-f006" class="html-fig">Figure 6</a>b); and (<b>c1</b>–<b>c4</b>) angulation misfit: the abutment rotates for 3 degrees (see <a href="#jfb-15-00344-f006" class="html-fig">Figure 6</a>c).</p>
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<p>FEM results for the angulation misfit (see <a href="#jfb-15-00344-f006" class="html-fig">Figure 6</a>c) of the long Ti implant (see <a href="#jfb-15-00344-f004" class="html-fig">Figure 4</a>b). Stresses are depicted as equivalent to von Mises stress, while strains represent the maximum principal strain. (<b>c1</b>–<b>c4</b>) angulation misfit: the abutment rotates for 3 degrees (see <a href="#jfb-15-00344-f006" class="html-fig">Figure 6</a>c), (<b>c5</b>) Detail of the flexible ball head (stress).</p>
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<p>FEM results for the long Nitinol implant, featuring an embedded flexible Nitinol long shaft (see <a href="#jfb-15-00344-f004" class="html-fig">Figure 4</a>b) for the angulation misfit (see <a href="#jfb-15-00344-f006" class="html-fig">Figure 6</a>c). Stresses are depicted as equivalent to von Mises stress, while strains represent the maximum principal strain. In (c5), the martensite volume fraction is mapped. (<b>c1</b>–<b>c4</b>) angulation misfit: the abutment rotates for 3 degrees (see <a href="#jfb-15-00344-f006" class="html-fig">Figure 6</a>c), (<b>c5</b>) detail of the flexible ball head (martensite volume fraction MVF).</p>
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<p>FEM results for the short Nitinol implant, featuring an embedded flexible Nitinol short shaft (see <a href="#jfb-15-00344-f004" class="html-fig">Figure 4</a>c) for the angulation misfit (see <a href="#jfb-15-00344-f006" class="html-fig">Figure 6</a>c). Stresses are depicted as equivalent to von Mises stress, while strains represent the maximum principal strain. (<b>c1</b>–<b>c4</b>) angulation misfit: the abutment rotates for 3 degrees (see <a href="#jfb-15-00344-f006" class="html-fig">Figure 6</a>c), (<b>c5</b>) Martensite volume fraction MVF.</p>
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<p>FEM results for the short-necked Nitinol implant, featuring a short-necked embedded Nitinol shaft (see <a href="#jfb-15-00344-f004" class="html-fig">Figure 4</a>d) in angulation misfit (see <a href="#jfb-15-00344-f006" class="html-fig">Figure 6</a>c). Stresses are depicted as equivalent to von Mises stress, while strains represent the maximum principal strain. (<b>c1</b>–<b>c4</b>) angulation misfit: the abutment rotates for 3 degrees (see <a href="#jfb-15-00344-f006" class="html-fig">Figure 6</a>c), (<b>c5</b>) Martensite volume fraction MVF.</p>
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<p>The effect of the ultimate design and material optimization on the reaction stresses on the surrounding Ti abutment. (<b>a1</b>,<b>b1</b>) The solid Ti implant and the flexible-necked Nitinol implant, respectively. In both trials, the implant is rotated (<math display="inline"><semantics> <mrow> <mi>θ</mi> <mo>=</mo> <mn>3</mn> </mrow> </semantics></math> degrees) and shifted horizontally by 0.1 mm in relation to the female part. (<b>a2</b>,<b>b2</b>) The resultant reaction stresses on the surrounding Ti abutment for the reference solid Ti design and the final optimized Nitinol implant design, respectively.</p>
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17 pages, 16140 KiB  
Article
An Investigation on the High-Temperature Stability and Tribological Properties of Impregnated Graphite
by Juying Zhao, Qi Xin, Yunshuang Pang, Xiao Ning, Lingcheng Kong, Guangyang Hu, Ying Liu, Haosheng Chen and Yongjian Li
Lubricants 2024, 12(11), 388; https://doi.org/10.3390/lubricants12110388 - 13 Nov 2024
Viewed by 349
Abstract
Impregnated graphite is a common material for friction pairs in aeroengine seals, especially at high temperatures. For the convenience of the application of graphite materials in aeroengines, an SRV-4 tribometer and a synchronous thermal analyzer are employed to study the tribological properties and [...] Read more.
Impregnated graphite is a common material for friction pairs in aeroengine seals, especially at high temperatures. For the convenience of the application of graphite materials in aeroengines, an SRV-4 tribometer and a synchronous thermal analyzer are employed to study the tribological properties and thermal stability of pure, resin-impregnated, metal-impregnated, and phosphate-impregnated graphite against stainless steel from room temperature to 500 °C. The results indicate that impregnations can improve the wear resistance and thermal stability of graphite at high temperatures. Compared with other impregnated graphite materials, the resin-impregnated graphite shows a good friction coefficient and poor wear rate and thermal stability over 300 °C, due to the degradation and oxidation of the resin-and-graphite matrix. The metal- and phosphate-impregnated graphite materials exhibit excellent wear resistance and thermal stability under 500 °C as a result of the protection of the impregnations, while the average friction coefficient of the metal-impregnated graphite is much greater than the phosphate-impregnated graphite, and even reaches 2.14-fold at 300 °C. The wear rates for the graphite impregnated with resin, metal, and phosphate are 235 × 10−7, 7 × 10−7, and 16 × 10−7 mm3N−1m−1 at 500 °C, respectively. Considering all aspects, the phosphate-impregnated graphite exhibits excellent tribological properties and thermal stability. Full article
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<p>Schematic diagram of friction test and test samples: (<b>a</b>) friction test and sliding directions; (<b>b</b>) stainless steel sample (left side—top view; right side—bottom view); (<b>c</b>) graphite sample.</p>
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<p>Friction coefficients of graphite materials under different working conditions. (<b>a</b>) Average friction coefficient; (<b>b</b>) pure graphite; (<b>c</b>) resin-impregnated graphite; (<b>d</b>) metal-impregnated graphite; (<b>e</b>) phosphate-impregnated graphite.</p>
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<p>The wear rates of the four graphite materials at different temperatures. (“×” indicates that the group did not undergo a friction test for safety reasons).</p>
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<p>Surface morphologies of four graphite materials under different working conditions. (The ellipsis indicates that the group has not undergone a friction test for safety reasons).</p>
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<p>Mass loss rates of different graphite materials after 5 h prolonged heating tests. (The blue arrow indicates the correlation between the weight loss percentage of the graphite and the images of the graphite samples after the tests).</p>
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<p>Test results of thermal stability for different graphite materials. (<b>a</b>) Thermogravimetric curves, (<b>b</b>) DSC curves, (<b>c</b>) FTIR curves.</p>
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<p>Normalized hardness of different graphite materials under high temperature.</p>
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<p>The SEM results of the pure graphite and resin-impregnated graphite at R.T. and 500 °C: (<b>a</b>) clean pure graphite at R.T., (<b>b</b>) worn pure graphite at R.T., (<b>c</b>) clean resin–graphite at R.T., (<b>d</b>) worn resin–graphite at R.T., (<b>e</b>) clean resin–graphite at 500 °C, (<b>f</b>) worn resin–graphite at 500 °C (400×), (<b>g</b>) worn resin–graphite at 500 °C (1000×).</p>
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<p>The SEM results of the metal-impregnated graphite at R.T. and 500 °C: (<b>a</b>) clean metal–graphite at R.T., (<b>b</b>) worn metal–graphite at R.T. (400×), (<b>c</b>) worn metal–graphite at R.T. (1000×), (<b>d</b>) clean metal–graphite at 500 °C, (<b>e</b>) worn metal–graphite at 500 °C (400×), (<b>f</b>) worn metal–graphite at 500 °C (1000×).</p>
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<p>Energy spectrum distribution of the worn area of the metal-impregnated graphite at R.T.: C (red), Sb (light green), O (dark green), Fe (light yellow), Ni (orange).</p>
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<p>Element distribution of the unworn area of metal impregnated graphite materials at 500 °C: C (red), Sb (light green), O (dark green), Fe (light yellow), Ni (orange).</p>
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<p>The SEM results of the phosphate-impregnated graphite at R.T. and 500 °C: (<b>a</b>) clean graphite at R.T., (<b>b</b>) worn graphite at R.T., (<b>c</b>) clean graphite at 500 °C, (<b>d</b>) worn graphite at 500 °C.</p>
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<p>Tribological properties of graphite materials.</p>
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28 pages, 8368 KiB  
Article
Classification-Based Parameter Optimization Approach of the Turning Process
by Lei Yang, Yibo Jiang, Yawei Yang, Guowen Zeng, Zongzhi Zhu and Jiaxi Chen
Machines 2024, 12(11), 805; https://doi.org/10.3390/machines12110805 - 13 Nov 2024
Viewed by 341
Abstract
The turning process is a widely used machining process, and its productivity has a significant impact on the cost and profit in industrial enterprises. Currently, it is difficult to effectively determine the optimum process parameters under complex conditions. To address this issue, a [...] Read more.
The turning process is a widely used machining process, and its productivity has a significant impact on the cost and profit in industrial enterprises. Currently, it is difficult to effectively determine the optimum process parameters under complex conditions. To address this issue, a classification-based parameter optimization approach of the turning process is proposed in this paper, which aims to provide feasible optimization suggestions of process parameters and consists of a classification model and several optimization strategies. Specifically, the classification model is used to separate the whole complex process into different substages to reduce difficulties of the further optimization, and it achieves high accuracy and strong anti-interference in the identification of substages by integrating the advantages of an encoder-decoder framework, attention mechanism, and major voting. Additionally, during the optimization process of each substage, Dynamic Time Warping (DTW) and K-Nearest Neighbor (KNN) are utilized to eliminate the negative impact of cutting tool wear status on optimization results at first. Then, the envelope curve strategy and boxplot method succeed in the adaptive calculation of a parameter threshold and the detection of optimizable items. According to these optimization strategies, the proposed approach performs well in the provision of effective optimization suggestions. Ultimately, the proposed approach is verified by a bearing production line. Experimental results demonstrate that the proposed approach achieves a significant productivity improvement of 23.43% in the studied production line. Full article
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<p>The flowchart of the proposed approach.</p>
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<p>The schematic diagram of the overlapped sliding window.</p>
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<p>The structure of the EDAMMV model.</p>
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<p>The schematic diagram of LSTM unit.</p>
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<p>The schematic diagram of major voting.</p>
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<p>The schematic diagram of the optimization method.</p>
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<p>The schematic diagram of the alignment task when n is 6 and m is 9.</p>
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<p>The comparison between real distribution and sampling distribution (30 samples).</p>
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<p>The picture of the data acquisition and turning machine. (<b>a</b>) The data acquisition of main shaft; (<b>b</b>) the data acquisition of turret; (<b>c</b>) the data acquisition of main shaft power; (<b>d</b>) the workpiece.</p>
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<p>The schematic diagram of nine stages in the turning process.</p>
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<p>The effects of main-relevant component number. (<b>a</b>) Cumulative contribution rate. (<b>b</b>) The performance of main-relevant component numbers on the training set and the testing set.</p>
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<p>The effects of overlapped sliding window size.</p>
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<p>The training process of EDAMMV model. (<b>a</b>) The loss curve of EDAMMV model on the training set. (<b>b</b>) MAPE curves during training process.</p>
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<p>Classification results of the turning process. (<b>a</b>) The classification results from time step 1 to 3400. (<b>b</b>) The classification results from time step 3401 to 6800. (<b>c</b>) The classification results from time step 6801 to 10,200. (<b>d</b>) The classification results from time step 10,201 to 13,600.</p>
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<p>The wear status analysis of Cutting Tool. (<b>a</b>) Effects of tool wear status on vibration. (<b>b</b>) Distance calculation by DTW.</p>
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<p>The calculation of envelopes.</p>
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<p>Envelopes of the turning process.</p>
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<p>The distribution of productive time in each substage among different workpieces.</p>
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<p>The optimization effect of the turning process.</p>
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