Nothing Special   »   [go: up one dir, main page]

You seem to have javascript disabled. Please note that many of the page functionalities won't work as expected without javascript enabled.
 
 
Sign in to use this feature.

Years

Between: -

Subjects

remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline

Journals

Article Types

Countries / Regions

remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline

Search Results (253)

Search Parameters:
Keywords = pin-on-disc

Order results
Result details
Results per page
Select all
Export citation of selected articles as:
19 pages, 6532 KiB  
Article
Effect of T6 Tempering on the Wear and Corrosive Properties of Graphene and B4C Reinforced Al6061 Matrix Composites
by Bharathiraja Parasuraman and Anthony Xavior Michael
J. Manuf. Mater. Process. 2025, 9(3), 82; https://doi.org/10.3390/jmmp9030082 - 5 Mar 2025
Viewed by 175
Abstract
This research study aims to evaluate the wear and corrosive behaviour of aluminum 6061 alloy hybrid metal matrix composites after reinforcing them with graphene (0.5, 1 wt.%) and boron carbide (6 wt.%) at varying weight percentages. The hybrid composites were processed through ball [...] Read more.
This research study aims to evaluate the wear and corrosive behaviour of aluminum 6061 alloy hybrid metal matrix composites after reinforcing them with graphene (0.5, 1 wt.%) and boron carbide (6 wt.%) at varying weight percentages. The hybrid composites were processed through ball milling and powder compaction, followed by a microwave sintering process, and T6 temper heat treatment was carried out to improve the properties. The properties were evaluated and analyzed using FE-SEM, Pin-on-Disc tribometer, surface roughness, salt spray test, and electrochemical tests. The results were evaluated prior to and subsequent to the T6 heat-treatment conditions. The T6 tempered sample S1 (Al6061-0.5% Gr-6% B4C) exhibits a wear rate of 0.00107 mm3/Nm at 10 N and 0.00127 mm3/Nm at 20 N for 0.5 m/s sliding velocity. When the sliding velocity is 1 m/s, the wear rate is 0.00137 mm3/Nm at 10 N and 0.00187 mm3/Nm at 20 N load conditions. From the Tafel polarization results, the as-fabricated (F) condition demonstrates an Ecorr of −0.789 and an Icorr of 3.592 µA/cm2 and a corrosion rate of 0.039 mm/year. Transitioning to the T6 condition further decreases Icorr to 2.514 µA/cm2, Ecorr value of −0.814, and the corrosion rate to 0.027 mm/year. The results show that an increase in the addition of graphene wt.% from 0.5 to 1 to the Al 6061 alloy matrix deteriorated the wear and corrosive properties of the hybrid matrix composites. Full article
Show Figures

Figure 1

Figure 1
<p>FE-SEM Microstructures of (<b>a</b>) Al6061 alloy powder; (<b>b</b>) B<sub>4</sub>C; (<b>c</b>) graphene; (<b>d</b>) TEM micrograph of graphene [<a href="#B21-jmmp-09-00082" class="html-bibr">21</a>].</p>
Full article ">Figure 2
<p>Graphical overview of the fabrication process for Al6061-Gr-B<sub>4</sub>C composites [<a href="#B21-jmmp-09-00082" class="html-bibr">21</a>].</p>
Full article ">Figure 3
<p>Wear rate analysis of Al6061-Gr-B<sub>4</sub>C at as-fabricated and T6 temper conditions. (<b>a</b>) Sliding velocity of 0.5 m/s, (<b>b</b>) sliding velocity of 1 m/s.</p>
Full article ">Figure 4
<p>Mass loss in g of Al6061-Gr-B<sub>4</sub>C at as-fabricated and T6 temper conditions. (<b>a</b>) Sliding velocity of 0.5 m/s, (<b>b</b>) sliding velocity of 1 m/s.</p>
Full article ">Figure 5
<p>COF analysis of Al6061-Gr-B<sub>4</sub>C at as-fabricated and T6 temper conditions. (<b>a</b>) Sliding Velocity of 0.5 m/s, (<b>b</b>) sliding velocity of 1 m/s.</p>
Full article ">Figure 6
<p>Time vs. frictional force analysis at a sliding velocity of 1 m/s of Al6061-Gr-B<sub>4</sub>C at as-fabricated and T6 temper conditions. (<b>a</b>) Load 10 N, (<b>b</b>) load 20 N.</p>
Full article ">Figure 7
<p>Worn surface micrograph of Al6061-Gr-B<sub>4</sub>C at as-fabricated and T6 temper conditions. (<b>a</b>) AA6061-F, (<b>b</b>) AA6061-T6, (<b>c</b>) S1-F, (<b>d</b>) S1-T6, (<b>e</b>) S2-F, (<b>f</b>) S2-T6 condition.</p>
Full article ">Figure 7 Cont.
<p>Worn surface micrograph of Al6061-Gr-B<sub>4</sub>C at as-fabricated and T6 temper conditions. (<b>a</b>) AA6061-F, (<b>b</b>) AA6061-T6, (<b>c</b>) S1-F, (<b>d</b>) S1-T6, (<b>e</b>) S2-F, (<b>f</b>) S2-T6 condition.</p>
Full article ">Figure 8
<p>EDAX Analysis with mapping of worn surface of Al6061-Graphene-B<sub>4</sub>C at as-fabricated and T6 temper conditions. (<b>a</b>) Fabricated, (<b>b</b>) T6 condition.</p>
Full article ">Figure 9
<p>Surface roughness analysis of Al6061-Gr-B<sub>4</sub>C at as-fabricated and T6 temper conditions.</p>
Full article ">Figure 10
<p>Salt spray corrosion analysis of Al6061-Graphene-B<sub>4</sub>C at as-fabricated and T6 temper conditions.</p>
Full article ">Figure 11
<p>SEM analysis of the corroded surface of Al6061-Graphene-B<sub>4</sub>C at as-fabricated and T6 temper conditions.</p>
Full article ">Figure 12
<p>Tafel polarization curves of Al6061-Graphene-B<sub>4</sub>C at as-fabricated and T6 temper conditions.</p>
Full article ">
18 pages, 4098 KiB  
Article
The Effect of Top-of-Rail Products Incorporating Environmentally Acceptable Solid Particles on Friction, Retentivity, Wear and Airborne Particle Emissions of Wheel–Rail Contact
by Rahma Boukhris, Ellen Bergseth, Ulf Olofsson, Johan Leckner and Roland Ardai
Machines 2025, 13(3), 200; https://doi.org/10.3390/machines13030200 - 28 Feb 2025
Viewed by 147
Abstract
Excessive friction at the wheel–rail contact can limit the lifespan of the wheels and rails. Meanwhile, insufficient friction can lead to increased braking distance, risking safety. Top-of-Rail (TOR) products are recognised for their potential to achieve intermediate friction levels at the wheel–rail contact [...] Read more.
Excessive friction at the wheel–rail contact can limit the lifespan of the wheels and rails. Meanwhile, insufficient friction can lead to increased braking distance, risking safety. Top-of-Rail (TOR) products are recognised for their potential to achieve intermediate friction levels at the wheel–rail contact and mitigate wear damages. However, the impact of these products on the airborne wear particles emitted from wheel–rail contact is not thoroughly evaluated. High particle concentration levels, particularly on underground train platforms, raise respiratory and cardiovascular health concerns. This research employs a pin-on-disc to study the effect of laboratory (environmentally acceptable) and commercial TOR products on friction, retentivity, wear, and airborne particle emissions at the wheel–rail interface. The results indicated that TOR products with higher retentivity offered a wider interval of desired intermediate friction levels. The TOR products significantly reduced particle emissions compared to the dry condition. TOR products can, therefore, be promising in controlling friction and mitigating wear and particle emissions at the wheel–rail interface. However, to achieve the benefits of these products, it is essential to tailor their chemical composition carefully. Full article
(This article belongs to the Special Issue Wheel–Rail Contact: Mechanics, Wear and Analysis)
Show Figures

Figure 1

Figure 1
<p>Schematic of the test equipment. (A) room air; (B) fan; (C) flow rate measurement point; (D) filter; (E) flexible tube; (F) inlet for clean air, measurement point; (G) closed box (chamber); (H) POD machine; (I) pin sample; (J) air outlet, particle measurement points; (K) condensation particle counter (CPC); (L) dead weight; (M) rotating disc sample; (N) air inside the box, well mixed. Adapted from Olofsson et al. [<a href="#B24-machines-13-00200" class="html-bibr">24</a>].</p>
Full article ">Figure 2
<p>Sketch of (<b>a</b>) the disc sample and (<b>b</b>) the pin sample [<a href="#B27-machines-13-00200" class="html-bibr">27</a>].</p>
Full article ">Figure 3
<p>Schematic of a Condensation Particle Counter (CPC).</p>
Full article ">Figure 4
<p>The coefficient of friction across 1080 m sliding distance.</p>
Full article ">Figure 5
<p>Mean coefficient of friction for dry and lubricated conditions over different sliding distances.</p>
Full article ">Figure 6
<p>Disk and pin mass losses for dry and lubricated conditions.</p>
Full article ">Figure 7
<p>Particle number concentration per cm<sup>3</sup> over 1080 m sliding distance.</p>
Full article ">Figure 8
<p>Total particle number (≥7 nm in size) for dry and lubricated conditions over different sliding distances.</p>
Full article ">Figure 9
<p>Regression curves for each independent variable.</p>
Full article ">
15 pages, 6805 KiB  
Article
Metallurgical and Mechanical Properties of Stellite 6 Deposition Developed Through Friction Surfacing Technique
by Mohammad Faseeulla Khan, Ramachandran Damodaram, Hussain Altammar and Gangaraju Manogna Karthik
Materials 2025, 18(5), 1003; https://doi.org/10.3390/ma18051003 - 25 Feb 2025
Viewed by 211
Abstract
Friction surfacing (FS) is a solid-state process for depositing metallurgically bonded coatings for corrosion and wear protection. It is particularly attractive for depositing coatings in materials that are difficult to fusion deposit. Stellite 6 is one such material, which is widely used as [...] Read more.
Friction surfacing (FS) is a solid-state process for depositing metallurgically bonded coatings for corrosion and wear protection. It is particularly attractive for depositing coatings in materials that are difficult to fusion deposit. Stellite 6 is one such material, which is widely used as a protective coating on steel structures to combat wear and corrosion. In the current study, Stellite 6 was successfully friction-surfaced on low carbon steel plates without using any preheating. The microstructures and wear behavior of Stellite 6 coatings produced using FS were comparatively investigated with those produced using the plasma transferred arc (PTA) process. The PTA coatings showed a cast microstructure consisting of γ-dendrites and an inter-dendritic carbide network. On the other hand, the FS coatings showed a wrought microstructure with dynamically recrystallized grains and fine, uniformly distributed carbide particles. The FS coatings also showed uniform composition across the coating thickness and were undiluted, while the PTA coatings showed significant dilution as well as strong local variations in chemistry. The FS coatings exhibited a 22% increase in hardness (550 HV) compared to the PTA coatings (450 HV). Pin-on-disc dry sliding wear tests showed that the FS coatings (1.205 mm3) were more wear resistant compared to the PTA coatings (6.005 mm3), highlighting their superior mechanical performance. This study uniquely demonstrates the feasibility of depositing Stellite 6 coatings using FS without the need for preheating or post-deposition heat treatments, while achieving superior microstructural refinement, hardness, and wear resistance compared to conventional PTA coatings. Full article
Show Figures

Graphical abstract

Graphical abstract
Full article ">Figure 1
<p>Schematic of the friction surfacing.</p>
Full article ">Figure 2
<p>Pin-on-disc wear test set-up.</p>
Full article ">Figure 3
<p>Optical micrographs of (<b>A</b>) hot rolled low carbon steel substrate and (<b>B</b>) cast Stellite 6 consumable rod. The inset in (<b>B</b>) shows the high magnification image with the EDS spot analysis location (1 and 2) indicated.</p>
Full article ">Figure 4
<p>Microstructures of the PTA coating (<b>A</b>) at low magnification and (<b>B</b>) at higher magnification.</p>
Full article ">Figure 5
<p>Photograph of friction surfaced Stellite 6 coating.</p>
Full article ">Figure 6
<p>(<b>A</b>) SEM microstructures of friction surface-coated samples and (<b>B</b>) magnified view of the friction surface coating.</p>
Full article ">Figure 7
<p>Macrograph images showing location of EDS spot analysis on PTA coatings (<b>A</b>) and FS coatings (<b>B</b>).</p>
Full article ">Figure 8
<p>X-Ray diffraction patterns of the consumable rod, friction surfacing, and plasma transfer arc coatings.</p>
Full article ">Figure 9
<p>TEM microstructures of coated samples: (<b>A</b>) Friction surfacing, (<b>B</b>) Plasma Transfer Arc Coating. The annotations in (<b>A</b>): 1—dislocation sub-cell formation; 2—Fine carbide particles; 3—fine grain microstructure; and 4a, 4b, 4c—grains with low, medium, and high dislocation densities, respectively. The annotations in (<b>B</b>): 1—interconnected carbide network and 2—coarse dendritic structure.</p>
Full article ">Figure 10
<p>Micro Vickers hardness plots across the coating/substrate interface of the FS- and PTA-coated samples.</p>
Full article ">Figure 11
<p>Optical microscope microstructures of the HAZ; (<b>A</b>) Friction surfacing and (<b>B</b>) PTA coatings.</p>
Full article ">Figure 12
<p>Results of pin-on-disc wear test at room temperature for the FS and PTA coatings.</p>
Full article ">Figure 13
<p>Surface morphology of PTA-coated sample after wear test: (<b>A</b>) SEM-SE Image, (<b>B</b>) SEM-BSE Image.</p>
Full article ">Figure 14
<p>Surface morphology of FS-coated sample after wear test; (<b>A</b>) SEM-SE Image, (<b>B</b>) SEM-BSE Image.</p>
Full article ">
17 pages, 14670 KiB  
Article
Effect of Porosity on Tribological Properties of Medical-Grade 316L Stainless Steel Manufactured by Laser-Based Powder Bed Fusion
by Germán Omar Barrionuevo, Magdalena Walczak, Patricio Mendez, Iván La Fé-Perdomo, Erika Chiluisa-Palomo, Wilson Navas-Pinto and Duncan E. Cree
Materials 2025, 18(3), 568; https://doi.org/10.3390/ma18030568 - 26 Jan 2025
Viewed by 759
Abstract
The potential of laser-based powder bed fusion (L-PBF) technology for producing functional components relies on its capability of maintaining or even improving the mechanical properties of the processed material. This improvement is associated with the microstructure resulting from the high thermal gradient and [...] Read more.
The potential of laser-based powder bed fusion (L-PBF) technology for producing functional components relies on its capability of maintaining or even improving the mechanical properties of the processed material. This improvement is associated with the microstructure resulting from the high thermal gradient and fast cooling rate. However, this microstructural advantage may be counterbalanced by the lack of full density, which could be tolerated to a certain degree for applications such as biomedical implants and medical equipment. In this study, medical-grade 316L stainless steel specimens with porosities ranging from 1.7 to 9.1% were additively manufactured by L-PBF using different combinations of laser power and scanning speeds. Tribological properties were evaluated by pin-on-disc testing in dry conditions against a silicon nitride test body and analyzed in the context of microstructural characterization by optical and electron microscopy. The results reveal that higher porosity allows for a diminishing wear rate, which is explained by the capacity of the pores to retain wear debris related with the three-body abrasion. This research provides practical insights into the design of medical wear-resistant components, thereby enhancing our understanding of the potential of L-PBF in the fields of materials science and biomedical engineering. Full article
(This article belongs to the Special Issue State of the Art in Materials for Additive Manufacturing)
Show Figures

Figure 1

Figure 1
<p>Schematic representation of the laser powder bed fusion process where the different types of porosity generated can be observed: section view (<b>top</b>) and top view (<b>bottom</b>).</p>
Full article ">Figure 2
<p>OM images showing the porosity levels of the 316L stainless steel processed by L-PBF using varying scanning speeds and laser power.</p>
Full article ">Figure 3
<p>Main effect plot of the laser power (P) and scanning speed (V) on the resulting mean porosity.</p>
Full article ">Figure 4
<p>SEM image showing the pore morphology and distribution of the sample S3.</p>
Full article ">Figure 5
<p>The effect of laser power and scanning speed on the resulting porosity (<b>a</b>) surface plot and (<b>b</b>) contour plot analysis.</p>
Full article ">Figure 6
<p>Variation of friction coefficient for the experimental design.</p>
Full article ">Figure 7
<p>Wear response, evaluation of volume loss, and wear rate.</p>
Full article ">Figure 8
<p>The 3D morphology features of the wear track produced on 316L SS processed with different porosity levels: (<b>a</b>) low porosity (S9), (<b>b</b>) medium porosity (S6), and (<b>c</b>) high porosity (S3). Maximum depths: −31.754, −19.446, and −59.436 µm, respectively.</p>
Full article ">Figure 9
<p>Representative nanoindentation response and OM of a sample with a low porosity level (Berkovich tip indenter).</p>
Full article ">Figure 10
<p>(<b>a</b>) Sample with high porosity level; (<b>b</b>) porosity due to lack of fusion; and (<b>c</b>) porosity with partially melted powder bed.</p>
Full article ">Figure 11
<p>(<b>a</b>) SEM micrograph of microporosity and (<b>b</b>) EDS analysis of the micropores.</p>
Full article ">Figure 12
<p>Wear tracks of different porosity levels: (<b>a</b>) low porosity (S9), (<b>b</b>) medium porosity (S6), and (<b>c</b>) high porosity (S3).</p>
Full article ">Figure 13
<p>Wear rate as a function of the porosity level of 316L stainless steel manufactured by L-PBF.</p>
Full article ">Figure 14
<p>EDS analysis of the wear track: (<b>a</b>) SEM image, (<b>b</b>) elemental mapping, and (<b>c</b>) spectrum of the 316L SS.</p>
Full article ">
14 pages, 7845 KiB  
Article
Abrasion Behaviour of Natural and Composite Polytetrafluoroethylene Seal Materials Against Stainless Steel in Lunar Regolith Conditions
by György Barkó, Gábor Kalácska, Tamás Bálint, Ádám Sarankó, Ádám Kalácska, Ewelina Ryszawa, László Székely and Zoltán Károly
Lubricants 2025, 13(2), 43; https://doi.org/10.3390/lubricants13020043 - 22 Jan 2025
Viewed by 548
Abstract
In this paper, the abrasive effects of lunar simulant regoliths (LHS-1, LMS-1) have been investigated. Sealing performance of different sealant pin materials on stainless steel has been tested by the pin-on-disc method. Pin materials included block types such as pure polytetrafluoroethylene (PTFE), composite [...] Read more.
In this paper, the abrasive effects of lunar simulant regoliths (LHS-1, LMS-1) have been investigated. Sealing performance of different sealant pin materials on stainless steel has been tested by the pin-on-disc method. Pin materials included block types such as pure polytetrafluoroethylene (PTFE), composite PTFE, as well as braided PTFE and hybrid-composite braided PTFE. Tribological properties were evaluated based on measured friction, wear, surface roughness and scanning electron micrographs. Most significant differences were observed in the sealing effect of the pins between the braided and the block-type pin materials. The stainless steel/pin pairs showed significantly higher (0.4–0.5) friction coefficients for the braided pins than the block ones (0.2–0.3), while there was not a significant difference in the abrasive effect of the different lunar regoliths. Although significant wear of the steel part occurred only with the block-type pins, this disadvantage was apparent in comparison with the braided pins. The abrasive particles caused deformation and eventually complete disintegration of the braided pins. Both the coefficient of friction and the wear could be estimated by a multiple linear regression model, in which different regolith size was the dominant independent parameter for the various pins. Full article
(This article belongs to the Special Issue Aerospace Tribology)
Show Figures

Figure 1

Figure 1
<p>(<b>a</b>) Schematics and (<b>b</b>) photo of modified pin-on-disc measurements.</p>
Full article ">Figure 2
<p>The effect of travelled distance on the coefficient of friction of steel and different sealing material pairs in the case of (<b>a</b>) LHS-1 and (<b>b</b>) LMS-1 lunar regolith simulants.</p>
Full article ">Figure 3
<p>Light microscopy image of steel discs after 15 min of abrasion test with (<b>a</b>) LHS-1 and (<b>b</b>) LMS-1 lunar simulant regoliths in the case of a composite PTFE packing hybrid pin material.</p>
Full article ">Figure 4
<p>Effect of travelled distance on wear in the case of different sealing materials for (<b>a</b>) LHS-1 and (<b>b</b>) LMS-1 lunar simulant regoliths.</p>
Full article ">Figure 5
<p>SEM images of block-type pin materials; (<b>a</b>) Ln pin and (<b>b</b>) Lc pin after 30 min pin-on-disc tests.</p>
Full article ">Figure 6
<p>Photos (10×) and 3D images, respectively, of the worn surfaces of pins (<b>a</b>,<b>b</b>) Pn/LMS-1 contact and (<b>c</b>,<b>d</b>) Pc/LHS-1 contact after 15 min pin-on-disc tests.</p>
Full article ">Figure 7
<p>Light microscopy images of steel discs after 30 min of abrasion testing with the LHS-1 lunar simulant regolith in the case of different pin materials; (<b>a</b>) Ln, (<b>b</b>) Lc, (<b>c</b>) Pn, (<b>d</b>) Pc.</p>
Full article ">Figure 8
<p>SEM images of steel discs after 30 min of abrasion testing with the LMS-1 lunar simulant regolith in the case of different pin materials; (<b>a</b>) Ln, (<b>b</b>) Lc, (<b>c</b>) Pn, (<b>d</b>) Pc.</p>
Full article ">
17 pages, 17631 KiB  
Article
Tribological Analysis of Laser-Textured WC-Co Against Ti6Al4V Under Dry and Lubricated Conditions for Different Sliding Times
by Javier Garcia-Fernandez, Moises Batista, Juan Manuel Vazquez-Martinez, Jorge Salguero, Irene Del Sol and Magdalena Ramirez-Peña
Lubricants 2025, 13(1), 36; https://doi.org/10.3390/lubricants13010036 - 15 Jan 2025
Viewed by 645
Abstract
Machining titanium alloys, particularly Ti6Al4V, pose significant challenges in manufacturing engineering. The combination of high strength and low thermal conductivity makes Ti6Al4V a particularly difficult material to machine. One of these difficulties is the rapid wear and short tool life of cutting tools, [...] Read more.
Machining titanium alloys, particularly Ti6Al4V, pose significant challenges in manufacturing engineering. The combination of high strength and low thermal conductivity makes Ti6Al4V a particularly difficult material to machine. One of these difficulties is the rapid wear and short tool life of cutting tools, which substantially increases manufacturing costs. To address this issue, the texturing of cutting tools, especially using laser-based techniques, has garnered significant attention due to its potential to enhance the tribological performance of textured surfaces. In this paper, by means of a groove design applied to a tungsten carbide (WC) disc by laser surface texturing (LST), its behavior and wear have been evaluated after subjecting it to tribological pin-on-flat tests by confronting it with Ti6Al4V pins with different reciprocating times (250 s, 500 s, 750 s and 1000 s) in lubricated and dry conditions. In addition, these same tests have been replicated without textures for comparison. Through conducting this research, we expect to gain new insights into texturing processes and their influence on friction and sliding behavior under lubricated conditions. Additionally, the study aims to evaluate how lubricant retention capacity varies to reduce friction and wear across different testing durations. The results show better behavior with textures, reaching a higher rate of volume loss in the titanium pins. The main conclusions obtained after these tests are that textures offer a better performance in tests up to 800 s. In addition, after this time, the lubricant begins to lose its properties, becoming an abrasive paste. Full article
Show Figures

Graphical abstract

Graphical abstract
Full article ">Figure 1
<p>High compressive pressure during machining.</p>
Full article ">Figure 2
<p>Microhardness test on textured surface at the top of the grooves.</p>
Full article ">Figure 3
<p>Tested surfaces (non-textured and textured with an orientation of 90°) with 250 s, 500 s, 750 s, and 1000 s reciprocating cycle.</p>
Full article ">Figure 4
<p>WC-Co substrates: (<b>a</b>) 90° texture and (<b>b</b>) non-texture and surface topography of textured specimen.</p>
Full article ">Figure 5
<p>Comparison of textured and non-textured samples tested under dry conditions with test durations of 250 s, 500 s, 750 s, and 1000 s.</p>
Full article ">Figure 6
<p>Comparison of textured and non-textured samples tested under lubricated conditions with test durations of 250 s, 500 s, 750 s, and 1000 s.</p>
Full article ">Figure 7
<p>Comparison of the coefficient of friction for textured and non-textured samples under dry and lubricated conditions at test durations: (<b>a</b>) 250 s, (<b>b</b>) 500 s, (<b>c</b>) 750 s, and (<b>d</b>) 1000 s.</p>
Full article ">Figure 8
<p>Coefficient of friction as a function of test duration for textured and non-textured samples in lubricated and dry conditions.</p>
Full article ">Figure 9
<p>Mass loss of the pins between the textured and non-textured samples in lubricated and dry conditions.</p>
Full article ">Figure 10
<p>Mixture of wear debris and lubricant at the ends of the sliding track in 1000 s test with texture.</p>
Full article ">Figure 11
<p>Wear effects on pins (Ti6Al4V) for dry tests.</p>
Full article ">Figure 12
<p>Wear effects on pins (Ti6Al4V) for lubricated tests.</p>
Full article ">Figure 13
<p>Details of wear in the pin with 1000 s, tested with texture sample and under lubricated conditions.</p>
Full article ">Figure 14
<p>Comparison of the textured footprint under lubricated conditions at (<b>a</b>) 750 s and (<b>b</b>) 1000 s.</p>
Full article ">
16 pages, 4414 KiB  
Article
Effect of Alternating Magnetic Field Treatment on the Friction/Wear Resistance of 20Cr2Ni4A Under Lubricated Conditions
by Sufyan Akram, Mose Bevilacqua, Anatolii Babutskyi and Andreas Chrysanthou
Metals 2025, 15(1), 69; https://doi.org/10.3390/met15010069 - 14 Jan 2025
Viewed by 457
Abstract
High-strength nickel–chromium steel (20Cr2Ni4A) is typically used in bearing applications. Alternating magnetic field treatment, which is based on the use of a magnetiser, and which is fast and cost-effective in comparison to conventional processes, was applied to the material to improve its wear [...] Read more.
High-strength nickel–chromium steel (20Cr2Ni4A) is typically used in bearing applications. Alternating magnetic field treatment, which is based on the use of a magnetiser, and which is fast and cost-effective in comparison to conventional processes, was applied to the material to improve its wear resistance. The results of pin-on-disc wear testing using a AISI 52100 alloy counter pin revealed a decrease in the specific wear rate of the treated samples by 58% and a reduction in the value of the coefficient of friction by 28%. X-ray diffraction analysis showed a small increase in the amount of martensite and higher surface compressive residual stresses by 28% leading to improved hardness. The observed changes were not induced thermally. The volume expansion by the formation of martensite was achieved at near room temperature and led to a further increase in compressive residual stresses. The significance of this study is that the improvement in the properties was achieved at a current density value that was two orders of magnitude higher than the threshold for phase transformation and dislocation movement. The reasons for the effect of the alternating magnetic field treatment on the friction and wear properties are discussed in terms of the contribution of the magnetic field to the austenite-to-martensite phase transformation and the interaction between the magnetic domain walls and dislocations. Full article
(This article belongs to the Special Issue Advances in Electromagnetic Processing of Metallic Materials)
Show Figures

Figure 1

Figure 1
<p>Schematic diagrams of (<b>a</b>) the AMF treatment for the pin-on-disc sample and (<b>b</b>) a plot of the magnetic flux density against time during AMF treatment.</p>
Full article ">Figure 2
<p>Diagram of POD 2 pin-on-disc tester: (A) balance weight, (B) load beam, (C) sample, (D) load cell, (E) wear pin (ball) and holder, (F) wear track radius micrometre adjustment, and (G) rotating sample table.</p>
Full article ">Figure 3
<p>Schematic representation of the model employed in the simulation: 1, spacer; 2, air; 3, windings (comprising 70 turns); 4, air magnetizer core; and 5, disc sample.</p>
Full article ">Figure 4
<p>(<b>a</b>) Variation in the coefficient of friction for untreated and AMF-treated disc specimens of high-strength Ni-Cr steel; (<b>b</b>) specific wear rate and the average coefficient of friction for the untreated and AMF-treated conditions.</p>
Full article ">Figure 5
<p>SEM wear tracks of the surface of untreated (<b>a</b>,<b>b</b>) and treated (<b>c</b>,<b>d</b>) high-strength Ni-Cr steel after 1 h of pin-on-disc testing.</p>
Full article ">Figure 6
<p>AFM surface topographic micrograph of the worn surface for untreated (<b>a</b>) and treated (<b>b</b>) high-strength Ni-Cr steel.</p>
Full article ">Figure 7
<p>Nanoindentation results of (<b>a</b>) hardness and H/E<sup>2</sup> and (<b>b</b>) loading–unloading curves of treated and untreated high-strength Ni-Cr steel.</p>
Full article ">Figure 8
<p>X-ray diffraction patterns of untreated (black) and AMF-treated (red) specimens of high-strength Ni-Cr steel.</p>
Full article ">Figure 9
<p>Calculation using QuickField 6 software of the eddy current density at the cylindrical surface of the sample.</p>
Full article ">
14 pages, 10817 KiB  
Article
Wear Resistance of B4C-TiB2 Ceramic Composite
by Pavol Švec
Lubricants 2025, 13(1), 35; https://doi.org/10.3390/lubricants13010035 - 14 Jan 2025
Viewed by 574
Abstract
The effects of microstructure and mechanical properties on the wear resistance of B4C-TiB2 ceramic composite were studied. The composite was hot pressed from a B4C-TiO2 precursor at a temperature range of 1800 and 1850 °C. Both the [...] Read more.
The effects of microstructure and mechanical properties on the wear resistance of B4C-TiB2 ceramic composite were studied. The composite was hot pressed from a B4C-TiO2 precursor at a temperature range of 1800 and 1850 °C. Both the relative density and amount of TiB2 secondary phase of the B4C-TiB2 composite increased with the amount of TiO2 sintering additive in B4C-TiO2 precursor. The hardness of the composite increased with a secondary phase portion up to 29.8 vol.% TiB2. However, the positive effect of TiB2 secondary phase on the fracture toughness of B4C-TiB2 composite was measured in the complete experimental range, with the highest average attained value of 7.51 MPa·m1/2. The wear resistance of B4C-TiB2 composite increased with both the hardness and fracture toughness. The best wear resistance was achieved with the composite with a higher hardness value of 29.74 GPa. This sample consisted of 29.8 vol.% TiB2 secondary phase and reached a fracture toughness value of 6.91 MPa·m1/2. The fracture-induced mechanical wear of B4C-TiB2 composite was the main wear mechanism during the pin-on-disc wear test. Transgranular fracture with pullout of the surface and micro-crack formation in the direction perpendicular to the wear direction was observed on the worn surfaces. Full article
Show Figures

Figure 1

Figure 1
<p>The effect of TiO<sub>2</sub> sintering additive concentration on the density of B<sub>4</sub>C-TiB<sub>2</sub> composite.</p>
Full article ">Figure 2
<p>The XRD pattern of B<sub>4</sub>C-TiB<sub>2</sub> ceramic composite sintered from B<sub>4</sub>C-TiO<sub>2</sub> precursors with 40 wt.% TiO<sub>2</sub>.</p>
Full article ">Figure 3
<p>Microstructure of B<sub>4</sub>C-TiB<sub>2</sub> ceramic composite with 29.8 vol.% TiB<sub>2</sub>.</p>
Full article ">Figure 4
<p>Microstructure of B<sub>4</sub>C-TiB<sub>2</sub> ceramic composite with 40.2 vol.% TiB<sub>2</sub>.</p>
Full article ">Figure 5
<p>EDS mapping of B<sub>4</sub>C-TiB<sub>2</sub> ceramic composite with 29.8 vol.% TiB<sub>2</sub>: (<b>a</b>) SEM image; (<b>b</b>) Distribution of B (K α<sub>1-2</sub>); (<b>c</b>) Distribution of Ti (K α<sub>1</sub>); (<b>d</b>) Distribution of C (K α<sub>1-2</sub>).</p>
Full article ">Figure 6
<p>The effect of TiO<sub>2</sub> sintering additive concentration on the TiB<sub>2</sub> secondary phase portion created in B<sub>4</sub>C-TiB<sub>2</sub> composite.</p>
Full article ">Figure 7
<p>The effect of TiB<sub>2</sub> secondary phase portion on the hardness of B<sub>4</sub>C-TiB<sub>2</sub> composite.</p>
Full article ">Figure 8
<p>The effect of TiB<sub>2</sub> secondary phase portion on the fracture toughness of B<sub>4</sub>C-TiB<sub>2</sub> composite.</p>
Full article ">Figure 9
<p>Vickers indentation morphology of B<sub>4</sub>C-TiB<sub>2</sub> composite with 40.2 vol.% TiB<sub>2</sub>, the length (a) of one radial crack.</p>
Full article ">Figure 10
<p>The effect of TiB<sub>2</sub> secondary phase portion on the wear rate of B<sub>4</sub>C-TiB<sub>2</sub> composite.</p>
Full article ">Figure 11
<p>The effect of hardness on the wear rate of B<sub>4</sub>C-TiB<sub>2</sub> composite.</p>
Full article ">Figure 12
<p>The effect of fracture toughness on wear rate of B<sub>4</sub>C-TiB<sub>2</sub> composite.</p>
Full article ">Figure 13
<p>Worn surface of B<sub>4</sub>C-TiB<sub>2</sub> composite with 29.8 vol.% TiB<sub>2</sub>: (<b>a</b>) grooves; (<b>b</b>) micro-cracks.</p>
Full article ">Figure 14
<p>Worn surface of B<sub>4</sub>C-TiB<sub>2</sub> composite with 40.2 vol.% TiB<sub>2</sub>: (<b>a</b>) grooves; (<b>b</b>) micro-cracks.</p>
Full article ">Figure 15
<p>The XRD pattern of B<sub>4</sub>C-TiB<sub>2</sub> ceramic composite with 29.8 vol.% TiB<sub>2</sub> after pin-on-disc wear test.</p>
Full article ">
23 pages, 6597 KiB  
Article
Enhanced Tribological Performance of Laser-Textured TiN-Coated Ti6Al4V Alloy Surfaces: A Comparative Study with Untextured Surfaces
by Arulkumar Muniyappan, Prem Ananth Muthuvel, Anandhavelu Sanmugam, Mohammad Ahmad Wadaan, Almohannad Baabbad, Nallal Muthuchamy and Kang Hyun Park
Processes 2025, 13(1), 204; https://doi.org/10.3390/pr13010204 - 13 Jan 2025
Viewed by 663
Abstract
Titanium alloy is widely used as a biomaterial due to its strength, lightweight nature, and corrosion resistance. Despite its strength and lightweight nature, its low wear resistance limits its uses in prosthetic components. Laser surface texturing (LST) was used to improve the wear [...] Read more.
Titanium alloy is widely used as a biomaterial due to its strength, lightweight nature, and corrosion resistance. Despite its strength and lightweight nature, its low wear resistance limits its uses in prosthetic components. Laser surface texturing (LST) was used to improve the wear resistance of titanium alloys by creating textured surfaces before applying protective coatings. A biocompatible TiN composite protective coating was applied using physical vapour deposition (PVD) with a thickness of 4 µm. Response surface methodology (RSM) was used to predict the tribological properties by varying input parameters such as material type (TI, T2, T3, and T4), load in N, and sliding velocity in m/s. A pin-on-disc tribometer was used to conduct a unidirectional sliding wear test based on the RSM design. Tribological properties were studied to determine the impact of laser texturing on the bonding strength of the coating. As a result, material type T4 exhibits an improved coefficient of friction and specific wear resistance under varying sliding velocity and load conditions compared to other material types. The study was further supported by an ANSYS simulation, which revealed stress reduction affecting the coefficient of friction and, consequently, wear. The textured surface topography, wear mechanisms, and coating compositions were examined using scanning electron microscopy. Full article
(This article belongs to the Special Issue Synthesis and Applications of Nanomaterials)
Show Figures

Graphical abstract

Graphical abstract
Full article ">Figure 1
<p>(<b>a</b>) Procured Ti<sub>6</sub>Al<sub>4</sub>V alloys, (<b>b</b>) machined specimens with dimensions of 28 mm × 10 mm.</p>
Full article ">Figure 2
<p>Methodology.</p>
Full article ">Figure 3
<p>Process flow of laser surface texturing.</p>
Full article ">Figure 4
<p>Ti<sub>6</sub>Al<sub>4</sub>V—textured uncoated; Ti<sub>6</sub>Al<sub>4</sub>V—untextured TiN-coated; Ti<sub>6</sub>Al<sub>4</sub>V—textured TiN-coated.</p>
Full article ">Figure 5
<p>Pin-on-disc tribometer.</p>
Full article ">Figure 6
<p>Steps to perform ANSYS simulation.</p>
Full article ">Figure 7
<p>TiN-coated Ti<sub>6</sub>Al<sub>4</sub>V alloy surface: (<b>a</b>) 2D image of coated surface; (<b>b</b>) histogram image; and (<b>c</b>) Abbott–Firestone curve.</p>
Full article ">Figure 8
<p>SEM images of Ti<sub>6</sub>Al<sub>4</sub>V alloy: (<b>a</b>) T1 before wear test, (<b>b</b>) T1 after wear test, (<b>c</b>) T2 before wear test, (<b>d</b>) T2 after wear test, (<b>e</b>) T3 before wear test, (<b>f</b>) T3 after wear test, (<b>g</b>) T4 before wear test, (<b>h</b>) T4 after wear test.</p>
Full article ">Figure 8 Cont.
<p>SEM images of Ti<sub>6</sub>Al<sub>4</sub>V alloy: (<b>a</b>) T1 before wear test, (<b>b</b>) T1 after wear test, (<b>c</b>) T2 before wear test, (<b>d</b>) T2 after wear test, (<b>e</b>) T3 before wear test, (<b>f</b>) T3 after wear test, (<b>g</b>) T4 before wear test, (<b>h</b>) T4 after wear test.</p>
Full article ">Figure 9
<p>EDX analysis: (<b>a</b>) T1 specimen, (<b>b</b>) T2 specimen, and (<b>c</b>) T4 specimen after wear test.</p>
Full article ">Figure 9 Cont.
<p>EDX analysis: (<b>a</b>) T1 specimen, (<b>b</b>) T2 specimen, and (<b>c</b>) T4 specimen after wear test.</p>
Full article ">Figure 10
<p>Friction coefficient for experimentally tested samples: (<b>a</b>) average friction coefficient versus load, (<b>b</b>) friction coefficient versus sliding velocity at 60 N, (<b>c</b>) friction coefficient versus sliding velocity at 80 N, and (<b>d</b>) friction coefficient versus sliding velocity at 100 N.</p>
Full article ">Figure 11
<p>Specific wear rate for experimentally tested samples: (<b>a</b>) specific wear rate versus applied load, (<b>b</b>) specific wear rate versus sliding velocity at 60 N, (<b>c</b>) specific wear rate versus sliding velocity at 80 N, and (<b>d</b>) specific wear rate versus sliding velocity at 100 N.</p>
Full article ">Figure 12
<p>Surface topography Ti<sub>6</sub>Al<sub>4</sub>V alloy samples: (<b>a</b>) T1 specimen, (<b>b</b>) T2 specimen, (<b>c</b>) T3 specimen, and (<b>d</b>) T4 specimen.</p>
Full article ">Figure 13
<p>Surface roughness values of T1, T2, T3, and T4.</p>
Full article ">Figure 14
<p>Wear analysis result of Ansys simulation: (<b>a</b>) reference sample, (<b>b</b>) untextured coated TiN, (<b>c</b>) textured uncoated TiN, (<b>d</b>) textured coated TiN.</p>
Full article ">Figure 15
<p>RSM for coefficients of friction: (<b>a)</b> actual versus predicted, (<b>b</b>) residuals versus normal probability, (<b>c</b>) run number versus residuals, (<b>d</b>) run number versus DFFITS, and (<b>e</b>) 3D surface plot.</p>
Full article ">Figure 16
<p>RSM for specific wear rate: (<b>a)</b> actual versus predicted, (<b>b</b>) residuals versus normal probability, (<b>c</b>) run number versus residuals, (<b>d</b>) run number versus DFFITS, and (<b>e</b>) 3D surface plot.</p>
Full article ">
16 pages, 3572 KiB  
Article
Study on the Effect of CeO2 on the Performance of WC + Ni60 Laser Cladding Coating
by Jingquan Wu, Jianwen Zhang, Dianlong Chen, Jiang Huang, Wenqing Shi, Fenju An and Xianglin Wu
Lubricants 2025, 13(1), 24; https://doi.org/10.3390/lubricants13010024 - 9 Jan 2025
Viewed by 769
Abstract
The aim of this investigation was to examine how CeO2 powder influences the performance of WC + Ni60 composite powder. Various cladding layers of WC + Ni60, incorporating differing mass fractions of CeO2, were created on the surface of Q235 [...] Read more.
The aim of this investigation was to examine how CeO2 powder influences the performance of WC + Ni60 composite powder. Various cladding layers of WC + Ni60, incorporating differing mass fractions of CeO2, were created on the surface of Q235 steel utilizing laser cladding technology. To analyze the microscopic structure of the resulting cladding layer, scanning electron microscopy was employed. Additionally, the abrasion and corrosion resistance properties were assessed through experimentation with a pin-and-disc friction and wear tester and an electrochemical workstation, respectively. The results of the study showed that when the mass fraction of CeO2 was 1%, the grain on the surface of the coating was refined, the carbide formation was reduced, and the uniformity of the cladding layer was the best. In terms of corrosion resistance, the coating with 1% CeO2 had a self-corrosion potential of 0.07 V and a self-corrosion current density of 1.82 × 10−5 A·cm−2, showing the best corrosion resistance, and the coating self-corrosion potential was higher than that of the coating and substrate without CeO2. In terms of abrasion resistance, coatings with 1% CeO2 had a lower coefficient of friction (0.47) and a smaller wear rate 0.034 mm3, and the wear amount was only 23.5% of that of coatings without CeO2, resulting in the best wear resistance. In conclusion, coatings containing 1% CeO2 exhibit the minimal coefficient of friction and the lowest wear rates, while simultaneously providing optimal corrosion resistance. Full article
(This article belongs to the Special Issue Wear-Resistant Coatings and Film Materials)
Show Figures

Figure 1

Figure 1
<p>Morphology and particle size distribution of mixed powder. (<b>a</b>) Ni60 material morphology, (<b>b</b>) Ni60 material size, (<b>c</b>) WC material morphology, (<b>d</b>) WC material size.</p>
Full article ">Figure 2
<p>Interface morphology with different amounts of CeO<sub>2</sub>. (<b>a</b>) Topography of the cross-section without CeO<sub>2</sub> and (<b>b</b>) 1% CeO<sub>2</sub>. (<b>c</b>) Cross-sectional morphology of 2% CeO<sub>2</sub>. (<b>d</b>) Enlarged view at the weld line without CeO<sub>2</sub> addition. (<b>e</b>) Enlarged view at the 1% CeO<sub>2</sub> weld line. (<b>f</b>) Enlarged view at the 2% CeO<sub>2</sub> weld line.</p>
Full article ">Figure 3
<p>XRD diffraction spectrum analysis. (<b>a</b>) Diffraction patterns of fused cladding layers with different contents of CeO<sub>2</sub>. (<b>b</b>) The main diffraction peak magnification shows a different amount of CeO<sub>2</sub>.</p>
Full article ">Figure 4
<p>Coating EDS scan points with different CeO<sub>2</sub> contents. (<b>a</b>) EDS scanning points without added CeO<sub>2</sub>. (<b>b</b>) EDS scanning points with 1% CeO<sub>2</sub> content. (<b>c</b>) EDS scanning points with 2% CeO<sub>2</sub> content.</p>
Full article ">Figure 5
<p>Microstructure with different CeO<sub>2</sub> contents. (<b>a</b>) 2000-fold microstructure without added CeO<sub>2</sub>. (<b>b</b>) 2000-fold microstructure containing 1% CeO<sub>2</sub>. (<b>c</b>) 2000-fold microstructure containing 2% CeO<sub>2</sub>.</p>
Full article ">Figure 6
<p>Friction and wear. (<b>a</b>) Coefficient of friction of each coating surface. (<b>b</b>) Wear profile. (<b>c</b>) Amount of wear.</p>
Full article ">Figure 7
<p>Scanning electron microscope (SEM) image after wear. (<b>a</b>) Post-wear morphology of fused cladding layer with CeO<sub>2</sub> mass fraction 0. (<b>b</b>) Post-wear morphology of fused cladding layer with CeO<sub>2</sub> mass fraction 1. (<b>c</b>) Fused cladding layer with CeO<sub>2</sub> mass fraction of 2 after abrasion. (<b>d</b>) Localized magnification of the furrows after abrasion of the fused cladding layer with a CeO<sub>2</sub> mass fraction of 0 by a factor of 2000. (<b>e</b>) Localized magnification of the furrows after the abrasion of the fused cladding layer with a CeO<sub>2</sub> mass fraction of 1 by a factor of 2000. (<b>f</b>) Localized magnification of the furrows after the abrasion of the fused cladding layer with a CeO<sub>2</sub> mass fraction of 2 by a factor of 2000.</p>
Full article ">Figure 8
<p>Polarization curves of cladding layers with different mass fractions of CeO<sub>2</sub>.</p>
Full article ">
13 pages, 51039 KiB  
Article
Effects of Sliding Speed on Wear Behavior of High-Velocity Oxygen Fuel-Sprayed FeCrMoNiCuBSiC Metallic Glass Coatings
by Lei Qiao, Botao Zhou, Ruifeng Li, Taotao Li, Yue Zhao, Xiaoqiang Zhang and Chul-Hee Lee
Lubricants 2025, 13(1), 10; https://doi.org/10.3390/lubricants13010010 - 30 Dec 2024
Viewed by 632
Abstract
A FeCrMoNiCuBSiC metallic glass coating was designed and then deposited by the high-velocity oxygen fuel (HVOF) spraying technique. X-ray diffraction, a scanning electron microscope, and a microhardness tester were applied to characterize the phase, microstructure, and mechanical properties of the coating. The amorphous [...] Read more.
A FeCrMoNiCuBSiC metallic glass coating was designed and then deposited by the high-velocity oxygen fuel (HVOF) spraying technique. X-ray diffraction, a scanning electron microscope, and a microhardness tester were applied to characterize the phase, microstructure, and mechanical properties of the coating. The amorphous phase was the main phase in the coating, and crystal phases were almost undetectable in the XRD results. The coating had a dense structure (the porosity was 1.47 ± 0.32%) and high Vickers microhardness (848 ± 22 HV0.3). The wear behavior of the coatings sliding against WC-Co was studied with a pin-on-disc wear test system and was compared with that of 316L stainless steel. The coating improved the wear resistance of the steel by around 7–9 times at different sliding speeds. As the sliding speed was increased, the wear loss rate of the steel obviously increased, yet the loss rate of the coating decreased first and then increased. This happened because the contact flash temperature induced by friction increases with the sliding speed, which results in oxidative behavior and crystallization events in the coating. The dominating wear mechanism of the coating is fatigue wear combined with oxidative wear. Full article
(This article belongs to the Special Issue Wear-Resistant Coatings and Film Materials)
Show Figures

Figure 1

Figure 1
<p>(<b>a</b>) Pin-on-disc wear testing machine; (<b>b</b>) illustration of a WC-Co pin rotating on the surface of the coating.</p>
Full article ">Figure 2
<p>XRD curves of the powder and deposited coating.</p>
Full article ">Figure 3
<p>SEM morphologies of cross-section of the Fe-based metallic glass coating: (<b>a</b>) low magnification; (<b>b</b>) high magnification.</p>
Full article ">Figure 4
<p>Microhardness–distance profile of the Fe-based metallic glass coating.</p>
Full article ">Figure 5
<p>COF vs. sliding time of the Fe-based coating (<b>a</b>) and 316L stainless steel (<b>b</b>).</p>
Full article ">Figure 6
<p>Macroscopic images of the Fe-based coating (<b>a</b>–<b>c</b>) and 316L stainless steel (<b>d</b>–<b>f</b>) after 4 h wear test at different sliding speeds: (<b>a</b>,<b>d</b>) 0.06 m/s; (<b>b</b>,<b>e</b>) 0.09 m/s; (<b>c</b>,<b>f</b>) 0.12 m/s.</p>
Full article ">Figure 7
<p>Surface profiles across the wear scars of the Fe-based coating (<b>a</b>), 316L stainless steel (<b>b</b>), and their comparison (<b>c</b>).</p>
Full article ">Figure 8
<p>Mass loss rates of the Fe-based coating and 316L stainless steel during the wear test (<b>a</b>) and after 4 h wear test (<b>b</b>).</p>
Full article ">Figure 9
<p>SEM micrographs of the wear scars of the Fe-based coatings at sliding speeds of 0.06 m/s (<b>a</b>,<b>b</b>), 0.09 m/s (<b>c</b>,<b>d</b>), and 0.12 m/s (<b>e</b>,<b>f</b>), (<b>a</b>,<b>c</b>,<b>e</b>): low magnification; (<b>b</b>,<b>d</b>,<b>f</b>): high magnification).</p>
Full article ">Figure 10
<p>SEM micrographs of 316L stainless steel at sliding speed of 0.09 m/s: (<b>a</b>) low magnification; (<b>b</b>) high magnification.</p>
Full article ">Figure 11
<p>Illustrations of the wear mechanism of the coating.</p>
Full article ">
13 pages, 3091 KiB  
Article
Optimisation of Clutch Disc Friction Material Using a Multi-Layer Perceptron Artificial Neural Network
by George Bălășoiu, Cristian Munteniță, Valentin Tiberiu Amortila and Larisa Titire
Polymers 2024, 16(24), 3588; https://doi.org/10.3390/polym16243588 - 22 Dec 2024
Viewed by 646
Abstract
This paper presents an analysis of four clutch disc friction materials (from different manufacturers) used in manual transmissions. Scanning electron microscopy and energy-dispersive X-ray spectroscopy were employed for the microstructural and chemical characterisation of the friction materials. To reveal the tribological properties of [...] Read more.
This paper presents an analysis of four clutch disc friction materials (from different manufacturers) used in manual transmissions. Scanning electron microscopy and energy-dispersive X-ray spectroscopy were employed for the microstructural and chemical characterisation of the friction materials. To reveal the tribological properties of the selected clutch discs, three measurements of the friction coefficient between the material and the cast iron disc were conducted. The findings were employed to construct an artificial neural network using Easy NN software (V 14), with the objective of optimising the friction material. The chemical composition of the friction materials was employed as the input data, whereas the minimum, maximum, and average values of the friction coefficient, as well as the temperature generated during friction, were utilised as the output data. To assess the efficacy of the neural network, the correlation between the importance of input data and their sensitivity to output data was examined. It was determined that the model with three hidden layers exhibited a notable correlation between the six most influential chemical elements and their sensitivity. Based on this neural model, the chemical composition of the friction disc materials was optimised using the “Query” mode, aiming to minimise discrepancies in friction coefficients and temperature development. Full article
(This article belongs to the Special Issue Emerging Trends in Polymer Engineering: Polymer Connect-2024)
Show Figures

Figure 1

Figure 1
<p>General structure of a manual transmission dry clutch.</p>
Full article ">Figure 2
<p>Types of friction discs: (<b>a</b>) paper-based friction material; (<b>b</b>) disc with molybdenum friction layer; (<b>c</b>) disc with graphite friction layer; (<b>d</b>) disc with elastomer friction layer; (<b>e</b>) disc with ceramic friction layer; (<b>f</b>) disc with carbon friction layer.</p>
Full article ">Figure 3
<p>Pin-on-disc configuration: (<b>a</b>) schematic representation of the pin-on-disc configuration; (<b>b</b>) test rig with pin-on-disc configuration.</p>
Full article ">Figure 4
<p>Optimisation process using ANN.</p>
Full article ">Figure 5
<p>EDX analysis of the clutch disc friction materials: (<b>a</b>) disc 1; (<b>b</b>) disc 2; (<b>c</b>) disc 3; (<b>d</b>) disc 4.</p>
Full article ">Figure 5 Cont.
<p>EDX analysis of the clutch disc friction materials: (<b>a</b>) disc 1; (<b>b</b>) disc 2; (<b>c</b>) disc 3; (<b>d</b>) disc 4.</p>
Full article ">Figure 6
<p>Mean COF values as function of clutch disc friction material.</p>
Full article ">Figure 7
<p>(<b>a</b>) Disc surface temperature variation as a function of disc friction material; (<b>b</b>) specific heats of the friction materials.</p>
Full article ">Figure 8
<p>SEM analysis of the clutch disc friction material contact surfaces after the tests: (<b>a</b>) disc 1; (<b>b</b>) disc 2; (<b>c</b>) disc 3; (<b>d</b>) disc 4.</p>
Full article ">Figure 9
<p>Artificial neural network: (<b>a</b>) error evolution in the training stage; (<b>b</b>) structure of the ANN model.</p>
Full article ">Figure 10
<p>Analysis of the relative importance and relative sensitivity of the artificial neural network: (<b>a</b>) analysis of the importance of the input elements for the output data; (<b>b</b>) analysis of the sensitivity of the output data to the input data.</p>
Full article ">
19 pages, 11868 KiB  
Article
Tribological Investigation of Polymer Composite Dynamic Shaft Seals in Extraterrestrial Applications
by Ádám Kalácska, Alexander Coen, Jean Carlos Poletto, Patrick De Baets and Gábor Kalácska
Lubricants 2024, 12(12), 451; https://doi.org/10.3390/lubricants12120451 - 18 Dec 2024
Viewed by 745
Abstract
Polymer seals are utilized in various engineering applications to prevent leakage and contamination. The study investigates the wear and friction behavior of PTFE-based dynamic rotary seals, targeting their usage in space applications. Pin-on-disc dry sliding wear tests were performed with 0.5 MPa contact [...] Read more.
Polymer seals are utilized in various engineering applications to prevent leakage and contamination. The study investigates the wear and friction behavior of PTFE-based dynamic rotary seals, targeting their usage in space applications. Pin-on-disc dry sliding wear tests were performed with 0.5 MPa contact pressure and 0.2 m/s sliding velocity combining different lip seal (PTFE, PTFE+GF+MoS2), packing (PTFE, PTFE+Aramid fiber+solid lubricant) and shaft materials (34CrNiMo6, PEEK) involving third-body lunar (LHS-1) and Martian regolith (MGS-1) simulants. To understand the different influences of extraterrestrial regolith simulants compared to commonly encountered abrasives on Earth, quartz sand was selected as a reference. Quartz soil resulted in lower wear rates but a similar coefficient of friction to other regoliths. In the case of lip seals, testing with LHS-1 on PEEK and testing with MGS-1 on steel resulted in the most severe wear. Post-mortem surface analysis revealed the effect of external abrasive particles on the wear process and the transfer layer formation. The surface analysis confirmed that both lunar and Martian regolith simulants resulted in significant embedded particles. Based on the wear performance results, the lip seals performed better, but installation with an external packing could further aid the tribosystem. Full article
(This article belongs to the Special Issue Modeling and Characterization of Wear)
Show Figures

Figure 1

Figure 1
<p>Particle diameter distribution in function of volume of (<b>a</b>) Lunar Highland regolith simulant [<a href="#B28-lubricants-12-00451" class="html-bibr">28</a>] and (<b>b</b>) Mart Global regolith simulant [<a href="#B29-lubricants-12-00451" class="html-bibr">29</a>].</p>
Full article ">Figure 2
<p>(<b>a</b>) Test setup and (<b>b</b>) model of pin-on-disc assembly with the installed regolith guide plates and ring.</p>
Full article ">Figure 3
<p>Wear rate [mm<sup>3</sup>/Nm] of tested lip seal materials.</p>
Full article ">Figure 4
<p>Effect of external abrasive particles on the wear of lip seal specimens. (<b>a</b>) PTFE on 34CrNiMo6 counterface, (<b>b</b>) PTFE+GF+MoS<sub>2</sub> on 34CrNiMo6 counterface, (<b>c</b>) PTFE on PEEK counterface, and (<b>d</b>) PTFE+GF+MoS<sub>2</sub> on PEEK counterface.</p>
Full article ">Figure 5
<p>(<b>a</b>) Optical microscopy and (<b>b</b>) 3D topography of PTFE lip seal sample tested on PEEK with MGS-1 regolith.</p>
Full article ">Figure 6
<p>Effect of external abrasive particles on the wear of packing specimens. (<b>a</b>) PTFE on 34CrNiMo6 counterface, (<b>b</b>) PTFE+AF on 34CrNiMo6 counterface, (<b>c</b>) PTFE on PEEK counterface, and (<b>d</b>) PTFE+AF on PEEK counterface.</p>
Full article ">Figure 7
<p>(<b>a</b>) Optical image and (<b>b</b>) 3D topography of the partially removed surface layer of a pure PTFE packing sample tested on 34CrNiMo6 steel with quartz sand.</p>
Full article ">Figure 8
<p>Effect of external abrasive particles on the coefficient of friction of lip seal specimens. (<b>a</b>) PTFE on 34CrNiMo6 counterface, (<b>b</b>) PTFE+GF+MoS<sub>2</sub> on 34CrNiMo6 counterface, (<b>c</b>) PTFE on PEEK counterface, and (<b>d</b>) PTFE+GF+MoS<sub>2</sub> on PEEK counterface.</p>
Full article ">Figure 9
<p>Effect of external abrasive particles on the coefficient of friction of packing specimens. (<b>a</b>) PTFE on 34CrNiMo6 counterface, (<b>b</b>) PTFE+AF on 34CrNiMo6 counterface, (<b>c</b>) PTFE on PEEK counterface, and (<b>d</b>) PTFE+AF on PEEK counterface.</p>
Full article ">Figure 10
<p>Post-mortem (<b>a</b>) macro image and (<b>b</b>) 3D surface topography of 34CrNiMo6 steel counterface tested in PTFE+GF+MoS<sub>2</sub> with LHS-1 regolith tribosystem.</p>
Full article ">Figure 11
<p>Post-mortem optical microscopy and corresponding 3D topography of tested pin specimens. (<b>a</b>,<b>b</b>) PTFE on steel counterface with quartz sand, (<b>c</b>,<b>d</b>) PTFE+GF+MoS<sub>2</sub> on steel counterface with LHS-1 lunar regolith, and (<b>e</b>,<b>f</b>) PTFE on steel counterface with MGS-1 regolith.</p>
Full article ">Figure 12
<p>Post-mortem (<b>a</b>) macro image and (<b>b</b>) 3D surface topography of PEEK counterface tested in PTFE+GF+MoS<sub>2</sub> with LHS-1 regolith tribosystem and the embedded LHS-1 particles in the PTFE+GF+MoS<sub>2</sub> pin: (<b>c</b>) optical image and (<b>d</b>) 3D topography.</p>
Full article ">Figure 13
<p>Post-mortem (<b>a</b>) macro image and (<b>b</b>) 3D surface topography of PEEK counterface tested in PTFE+GF+MoS<sub>2</sub> with MGS-1 regolith tribosystem and the embedded MGS-1 particles in the PTFE+GF+MoS<sub>2</sub> pin: (<b>c</b>) optical image and (<b>d</b>) 3D topography.</p>
Full article ">Figure 14
<p>Post-mortem (<b>a</b>) macro image and (<b>b</b>) 3D surface topography of PEEK counterface tested with PTFE and quartz sand and the embedded several quartz particles in the PTFE pin: (<b>c</b>) optical image and (<b>d</b>) 3D topography.</p>
Full article ">Figure 15
<p>(<b>a</b>) Macro image of PEEK counterface, (<b>b</b>) macro image of PTFE+AF packing sample, (<b>c</b>) optical microscopy, and (<b>d</b>) 3D topography of the wear track on PEEK tested with quartz.</p>
Full article ">
17 pages, 45748 KiB  
Article
Utilization of Magnetic Fraction Isolated from Steel Furnace Slag as a Mild Abrasive in Formulation of Cu-Free Friction Composites
by Vlastimil Matějka, Priyadarshini Jayashree, Kryštof Foniok, Jozef Vlček, Petra Matějková and Giovanni Straffelini
Lubricants 2024, 12(12), 440; https://doi.org/10.3390/lubricants12120440 - 10 Dec 2024
Viewed by 754
Abstract
Magnetic fraction isolated from steel furnace slag was tested as a component of Cu-free friction composites. The friction–wear performance and production of wear particles during their testing using a pin-on-disc tester against a cast iron disc were evaluated. To compare the effect of [...] Read more.
Magnetic fraction isolated from steel furnace slag was tested as a component of Cu-free friction composites. The friction–wear performance and production of wear particles during their testing using a pin-on-disc tester against a cast iron disc were evaluated. To compare the effect of the magnetic fraction on the parameters studied, the composite with alumina and the composite with original steel furnace slag were also prepared and tested. All composites showed a comparable friction coefficient. The composite with original steel furnace slag, and the composite with a magnetic fraction showed higher wear resistance compared to the composite containing alumina. The positive effect of the magnetic fraction on the extent of the emission of wear particles was observed and explained by the decreased aggressiveness of this composite to the cast iron disc. The influence of the phase composition of the steel furnace slag and the magnetic fraction on the friction film formation was also indicated, and its effect on the production of wear particles was proposed. Full article
Show Figures

Graphical abstract

Graphical abstract
Full article ">Figure 1
<p>2D (<b>a</b>) and 3D (<b>b</b>) images of the disc surface after polishing.</p>
Full article ">Figure 2
<p>Images of (<b>a</b>) the PoD tester used for tests and (<b>b</b>) details of the chamber.</p>
Full article ">Figure 3
<p>X-ray diffraction patterns of SFS and MFS.</p>
Full article ">Figure 4
<p>SEM micrographs of (<b>a</b>) SFS, (<b>b</b>) MFS, and (<b>c</b>) alumina.</p>
Full article ">Figure 5
<p>Images of the surfaces of the prepared pins (<b>a</b>) FC–Al, (<b>b</b>) FC–SFS, and (<b>c</b>) FC–MFS. (Orange arrows show the presence of pores).</p>
Full article ">Figure 6
<p>2D images of the surfaces of the prepared pins of composites FC–Al (<b>a</b>), FC–SFS, (<b>b</b>) and FC–MFS (<b>c</b>), and respective 3D images of the given area with the calculated roughness values below the 2D images.</p>
Full article ">Figure 7
<p>Typical CoF curves of FC–Al, FC–SFS, and FC–MFS (<b>a</b>); details of the instantaneous CoF values in the region of 4000–5400 s (<b>b</b>).</p>
Full article ">Figure 8
<p>Comparison of CoF values (<b>a</b>), values of specific wear coefficients (<b>b</b>), and particle number concentrations (<b>c</b>).</p>
Full article ">Figure 9
<p>Worn pin surfaces of (<b>a</b>) FC–Al, (<b>b</b>) FC–SFS, and (<b>c</b>) FC–MFS. (The orange arrows show the typical areas covered by secondary contact plateaus, and the orange rectangles indicate the area selected for EDX analysis).</p>
Full article ">Figure 10
<p>The typical LSCM images of secondary contact plateaus observed for (<b>a</b>) FC–Al, (<b>b</b>) FC–SFS, and (<b>c</b>) FC–MFS and respective 3D images of these areas.</p>
Full article ">Figure 11
<p>Wear track on the disc surface after the test with FC–SFS (<b>a</b>) and FC–MFS (<b>b</b>).</p>
Full article ">Figure 12
<p>Details of the 3D topography of the discs’ surfaces after the PoD test with MC–SFS (<b>a</b>) and MC–MFS (<b>b</b>).</p>
Full article ">Figure 13
<p>Comparison of the worn disc and the FC–SFS pin surface after PoD test. (<b>a</b>) Image of the wear track on the disc surface, (<b>b</b>) SE image of the details, showing a thick layer of friction film deposited on the wear track, (<b>c</b>) BSE image of the same area, (<b>d</b>) EDS spectrum obtained from the marked area, (<b>e</b>) BSE image of the details of the surface of the FC–SFS pin after PoD test showing typical secondary contact plateau, and (<b>f</b>) EDS spectrum obtained from the marked area.</p>
Full article ">Figure 14
<p>Comparison of the worn disc and the FC–MFS pin surface after PoD test. (<b>a</b>) Image of the wear track on the disc surface, (<b>b</b>) SE image showing collected wear particles deposited in the craters, (<b>c</b>) BSE image of the same area, (<b>d</b>) EDS spectrum obtained from the marked area, (<b>e</b>) BSE image of the details of the surface of the FC–MFS pin after PoD test showing a typical secondary contact plateau, and (<b>f</b>) EDS spectrum obtained from the marked area.</p>
Full article ">
14 pages, 97256 KiB  
Article
In Situ Operando Indicator of Dry Friction Squeal
by Maël Thévenot, Jean-François Brunel, Florent Brunel, Maxence Bigerelle, Merten Stender, Norbert Hoffmann and Philippe Dufrénoy
Lubricants 2024, 12(12), 435; https://doi.org/10.3390/lubricants12120435 - 8 Dec 2024
Viewed by 826
Abstract
In various applications, dry friction could induce vibrations. A well-known example is frictional braking systems in ground transportation vehicles involving a sliding contact between a rotating and a stationary part. In such scenarios, the emission of high-intensity noise, commonly known as squeal, can [...] Read more.
In various applications, dry friction could induce vibrations. A well-known example is frictional braking systems in ground transportation vehicles involving a sliding contact between a rotating and a stationary part. In such scenarios, the emission of high-intensity noise, commonly known as squeal, can present human health risks based on the noise’s intensity, frequency, and occurrences. Despite the importance of squeal in the context of advancing urbanization, the parameters determining its occurrence remain uncertain due to the complexity of the involved phenomena. This study aims to identify a relevant operando indicator for predicting squeal occurrences. To this end, a pin-on-disc test rig was developed to replicate various contact conditions found in road profiles and investigate resulting squealing. Each test involves a multimodal instrumentation, complemented by surface observations. It is illustrated that the enhanced thermal indicator identified is relevant because it is sensitive to the thermomechanical and tribological phenomena involved in squealing. Full article
(This article belongs to the Special Issue Tribology in Vehicles)
Show Figures

Figure 1

Figure 1
<p>(<b>a</b>) Schematic representation of parts in contact. (<b>b</b>) Stationary part: pin of friction material mounted on aluminum blade. (<b>c</b>) Rotating part: steel disc with contact location.</p>
Full article ">Figure 2
<p>Test conditions investigated in this study in terms of rotation speed of the disc and pin’s axial displacement. Duration of test (ON) and between each test (OFF) are indicated in blue in seconds and pin’s surface observations with red dots.</p>
Full article ">Figure 3
<p>(<b>a</b>) Top view of the test bench presenting the pin’s positions for test and observation. (<b>b</b>) Front view of the pin in testing position.</p>
Full article ">Figure 4
<p>Profilometry observation of the pin before tests. (<b>a</b>) Image of the 20 mm × 20 mm pin’s surface, with some brighter patterns highlighted. (<b>b</b>) Shape of the pin’s surface. (<b>c</b>) Pin’s profilometry without the shape.</p>
Full article ">Figure 5
<p>Thermomechanical conditions investigated, resulting from the imposed test conditions.</p>
Full article ">Figure 6
<p>Evolution of the surface roughness parameter S5p during the test campaign.</p>
Full article ">Figure 7
<p>Classes of surface topography observed with a zoomed area of each corresponding image: (<b>A</b>) very rough aspect, (<b>B</b>) rough with a noticeable friction direction, (<b>C</b>) clear sliding direction and smaller high differences, (<b>D</b>) rather smooth surface with a local porosity.</p>
Full article ">Figure 8
<p>Classification of the profilometry observations through the test campaign.</p>
Full article ">Figure 9
<p>Overall acoustic results during the campaign: squeal detection for each frequency &gt; 70 dB, disc’s rotating speed and maximal temperature of the pin.</p>
Full article ">Figure 10
<p>Classification of noise emissions for individual test. (<b>a</b>) 2.1 kHz squeal, (<b>b</b>) 3.3 kHz squeal, (<b>c</b>) 5.3 kHz squeal, (<b>d</b>) 18 kHz squeal.</p>
Full article ">Figure 11
<p>Classes of noise emissions observed for each test through the campaign, with rotating speed of the disc and pin temperature.</p>
Full article ">Figure 12
<p>Representation of frequency classes regarding maximum temperature of the pin, with surface classes for corresponding profilometry observation.</p>
Full article ">Figure 13
<p>Temperature difference of pin thermocouples for tests 240 to 526, regarding the maximal pin temperature.</p>
Full article ">
Back to TopTop