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J. Manuf. Mater. Process., Volume 4, Issue 4 (December 2020) – 28 articles

Cover Story (view full-size image): Manufacturing companies are exposed to increased complexity and competition. To stay competitive, companies need to minimize the total cost of quality while ensuring high transparency about process–product relationships within the manufacturing system. In this context, the development of technologies such as advanced analytics and cyber-physical production systems offers a promising approach. This paper discusses and defines essential elements of virtual quality gates in the context of manufacturing systems. To support the planning and implementation of virtual quality gates, a morphological box is developed which can be used to identify and derive an individual approach for a virtual quality gate based on the specific characteristics and requirements of the respective manufacturing system. Moreover, the framework is exemplified by three case studies from various industries, and resulting potentials [...] Read more.
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15 pages, 9688 KiB  
Article
Difficult Cutting Property of NiTi Alloy and Its Mechanism
by Hiroo Shizuka, Katsuhiko Sakai, Hao Yang, Kazuki Sonoda, Tetsuo Nagare, Yuji Kurebayashi and Kunio Hayakawa
J. Manuf. Mater. Process. 2020, 4(4), 124; https://doi.org/10.3390/jmmp4040124 - 18 Dec 2020
Cited by 10 | Viewed by 3009
Abstract
This paper describes the difficult machinability of nickel titanium alloy (NiTi alloy) and its mechanism. As a result of examining the difficult cutting machinability via a turning experiment, NiTi alloy cutting showed larger cutting force, higher cutting temperature, and severe tool wear with [...] Read more.
This paper describes the difficult machinability of nickel titanium alloy (NiTi alloy) and its mechanism. As a result of examining the difficult cutting machinability via a turning experiment, NiTi alloy cutting showed larger cutting force, higher cutting temperature, and severe tool wear with plastic deformation of the tool compared to Ti-6Al-4V. In addition, the discharged chips were tangled with the jaw chuck and the cutting tool. As a result of investigating the cause of these difficult machining properties by orthogonal cutting, it was found that the progression of severe flank wear is affected by the elastic recovery due to the super elasticity of the material. The verification of the results according to the shear plane theory suggest that the large deformation resistance of the material is the cause of the increase in cutting temperature. Furthermore, because the cutting temperature exceeds the shape memory transformation temperature, the generated chips are shape memory processed. It was also found that because the generated chips are super elastic, chips are not easily broken and they are lengthened, and are easily entangled with a cutting tool and a jaw chuck. Full article
(This article belongs to the Special Issue Progress in Precision Machining)
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<p>Schematic of an orthogonal cutting.</p>
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<p>Schematic of an orthogonal cutting.</p>
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<p>Cutting temperature at different cutting speeds for various materials.</p>
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<p>Relationship between the cutting speed and force.</p>
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<p>Pictures of tool wear at different cutting speeds and for cutting NiTi and Ti-6Al-4Vs. (<b>a</b>) Top view, (<b>b</b>) side view, (<b>c</b>) tip nose.</p>
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<p>Relationship between the cutting speed and flank wear.</p>
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<p>Measured cutting temperature in orthogonal cutting.</p>
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<p>Waveforms of cutting forces measured in the orthogonal cutting of NiTi alloy (v = 20 m/min, f = 0.05 mm/rev, t = 2 mm).</p>
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<p>Cutting force with relief angle change in orthogonal cutting (v = 20 m/min, f = 0.05 mm/rev, t = 2 mm).</p>
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<p>Cutting ratio calculated from the shear surface theory.</p>
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<p>Shear angle calculated from the shear surface theory.</p>
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<p>Shear stress and normal stress calculated from the shear surface theory.</p>
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<p>Coefficient of friction calculated from the shear surface theory.</p>
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<p>Tangling of chips with the jaw chuck and the cutting tool (v = 50 m/min, f = 0.1 mm/rev, t = 1.0 mm).</p>
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<p>Experiment to evaluate the shape memory effect of the chip. (<b>A</b>) original chip shape or unloading the thensile load (<b>B</b>) applying the tensile load at room temperature (<b>C</b>) cooling the chip on dry ice (<b>D</b>) applying the tensile load after cooling the chip (<b>E</b>) dipping the chip of D in water.</p>
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<p>Results of XPS analysis of the chips.</p>
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<p>Change in chip shape at different cutting speeds.</p>
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<p>High-speed camera observation of the chip discharge state (<b>left</b>: v 25 m/min, <b>right</b>: v 100 m/min).</p>
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<p>Shape memory mechanism of chip (left: v 25 m/min, right: v 100 m/min).</p>
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20 pages, 8098 KiB  
Article
Evaluation of Optimization Parameters of Semi-Solid Metal 6063 Aluminum Alloy from Friction Stir Welding Process Using Factorial Design Analysis
by Chaiyoot Meengam and Kittima Sillapasa
J. Manuf. Mater. Process. 2020, 4(4), 123; https://doi.org/10.3390/jmmp4040123 - 17 Dec 2020
Cited by 14 | Viewed by 4009
Abstract
The semi-solid-metal 6063 aluminum alloy was developed for the automotive industry. The objective of this research was to optimize parameters in friction stir welding process that can provide the highest tensile strength. The ANOVA factorial design was used to analyze rotation speed, welding [...] Read more.
The semi-solid-metal 6063 aluminum alloy was developed for the automotive industry. The objective of this research was to optimize parameters in friction stir welding process that can provide the highest tensile strength. The ANOVA factorial design was used to analyze rotation speed, welding speed, and tool geometry at different factor levels of experimentation. The results showed that the optimized tensile strength was 120.7 MPa from the cylindrical tool, rotation speed was from 1300 to 2100 rpm, and welding speed less than 75 mm/min in the coefficient of determination R2 was 95.09%, as can be considered from the regression equation. The examination of the stir-zone and thermal mechanical affected zone using SEM and EDX showed that the new recrystallization of the microstructure causes fine grain in the stir-zone, coarse grain in advancing-side thermal mechanical affected zone, and equiaxed grain in the retracting-side thermal-mechanical affect zone. The intermetallic compounds of β-Al5FeSi phase transformation phase were formed to three types, i.e., β″-Al5Fe, Mg2Si, and Al8Fe2Si phase were observed. Moreover, in the stir-zone and thermal-mechanical-affected zone, defects were found such as flash defects, void or cavity defects, crack defects, lack of penetration defects, tunnel defects, kissing bond defects, and dendrite formation defects affecting weldability. Full article
(This article belongs to the Special Issue Advanced Joining Processes and Techniques)
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<p>A globular microstructure of base SSM 6063 aluminum alloys.</p>
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<p>Different tool pin geometry for friction stir welding process (FSWp) of SSM 6063 aluminum alloys: (<b>a</b>) cylindrical, (<b>b</b>) triangular, (<b>c</b>) square, and (<b>d</b>) pentagon.</p>
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<p>The schematic view of the steps for principle FSWp of SSM 6063 aluminum alloys.</p>
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<p>Schematic diagram of FSWp of SSM 6063 aluminum alloys as (<b>a</b>) FSW sample, (<b>b</b>) tensile strength sample, and (<b>c</b>) hardness sample.</p>
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<p>The contour plot of tensile strength vs. <span class="html-italic">R</span>, <span class="html-italic">W</span>, and <span class="html-italic">T</span> of the welded on FSWp of SSM 6063 aluminum alloys.</p>
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<p>The stress–strain of the welded joint on FSWp of SSM 6063 aluminum alloys.</p>
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<p>Vicker’s hardness profiles: (<b>a</b>) Vicker’s hardness profiles in the cross-section of the welded on FSWp of SSM 6063 aluminum alloys and (<b>b</b>) Plot graph between Vicker’s hardness profiles and Distance from SZ center.</p>
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<p>The photography of microstructure in the joint from rotation speed 1320 rpm, welding speed 60 mm/min, and cylindrical tool. (<b>a</b>–<b>i</b>) nine different types of microstructural changes were observed under microscope.</p>
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<p>The six patterns of the defects of SSM 6063 aluminum alloy after FSWp in many different conditions for this experiment: (<b>a</b>) the flash defects, (<b>b</b>) the void or cavity defects, (<b>c</b>) the crack defects, (<b>d</b>) lack of penetration and tunnel defects, (<b>e</b>) the kissing bond defects, and (<b>f</b>) the dendrite formation defects.</p>
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<p>The evaluated of the microstructure in the welded joint by SEM from cylindrical tool, rotation speed at 1320 rpm, and welding speed at 60 mm/min. (<b>a</b>–<b>f</b>) six patterns of microstructural changes were observed.</p>
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<p>The micrographic mapping image by EDX spectroscopy of the welded joint: (<b>a</b>) the presence of SEM micrographs, (<b>b</b>) the presence of element phase maps, (<b>c</b>) the presence of aluminum element, (<b>d</b>) the presence of silicon element, (<b>e</b>) the presence of iron element, (<b>f</b>) the presence of manganese element, (<b>g</b>) the presence of carbon element, and (<b>h</b>) the present of EDX results of the secondary phase.</p>
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19 pages, 3220 KiB  
Article
Experimental and Numerical Assessment of the Hot Sheet Formability of Martensitic Stainless Steels
by Peter Birnbaum, Enrique Meza-García, Pierre Landgraf, Thomas Grund, Thomas Lampke and Verena Kräusel
J. Manuf. Mater. Process. 2020, 4(4), 122; https://doi.org/10.3390/jmmp4040122 - 16 Dec 2020
Cited by 3 | Viewed by 2350
Abstract
Hot formed sheet components made of Martensitic Stainless Steels (MSS) can achieve ultra-high strengths in combination with very high corrosion resistance. This enables to manufacture complex lightweight sheet components with longer lifespan. Nevertheless, the hot formability of MSS sheets has not been accurately [...] Read more.
Hot formed sheet components made of Martensitic Stainless Steels (MSS) can achieve ultra-high strengths in combination with very high corrosion resistance. This enables to manufacture complex lightweight sheet components with longer lifespan. Nevertheless, the hot formability of MSS sheets has not been accurately evaluated considering high temperatures and complex stress and strain states. In this work, the hot sheet formability of three MSS alloys under thermomechanical process conditions was investigated. Initially, mechanical properties of this sheet material were determined by uniaxial tensile test. Finite Element Method (FEM) simulation of a hot deep drawing process was performed under consideration of thermo physical calculated material models using the software JMatPro® and Simufact Forming® 15.0. The resulting strains and cooling rates developed locally in the work piece during the forming process were estimated. The numerical results were validated experimentally. Round cups were manufactured by hot deep drawing process. The resulting maximum drawing depth and hardness were measured. In general, all three alloys developed very good formability at forming temperatures between 700 and 900 °C and increased hardness values. However, they are highly susceptible to chemical composition, austenitization temperature, dwell time, and flange gap. A statistic approach is given to explain the correlation between hardness and its influencing factors. Full article
(This article belongs to the Special Issue Metal Forming and Joining)
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<p>Temperature-time curve of thermomechanical treatment for X12Cr13, X30Cr13 and X46Cr13.</p>
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<p>Deep drawing tool mounted in press (<b>a</b>) and CAD design of the deep drawing tool (<b>b</b>).</p>
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<p>Displacement by time and force by time during an exemplary deep drawing experimental trial.</p>
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<p>Detail of the force drop indicating the exact position where the depth position of the punch is located. The point of intersection indicates the maximum drawing depth.</p>
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<p>(<b>a</b>) Exemplary illustration of the area for hardness measurement on a cut cup, (<b>b</b>) Hardness curve HV1 of X46Cr13 after austenitization at 1150 °C for 120 s and subsequent forming at 900 °C.</p>
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<p>Exemplary cooling behavior of X12Cr13 and X46Cr13 after austenitizing at 1050 °C for 300 s and subsequent cooling in still air.</p>
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<p>Thermophysically calculated isothermal phase transformation diagrams (TTT) and M23C6 precipitations of the materials (<b>a</b>) X12Cr13, (<b>b</b>) X30Cr13 and (<b>c</b>) X46Cr13 after austenitization at 1050 °C and ASTM grain size = 9 using JMatPro<sup>®</sup>.</p>
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<p>Maximum drawing force during forming of cups made of the alloy X12Cr13, X30Cr13, and X46Cr13 at initial forming temperatures of 700 °C, 800 °C and 900 °C; blank diameter 170 mm; drawing depth 40 mm; drawing speed 20 mm/s; and an initial austenitization at 1050 °C for 300 s.</p>
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<p>Maximum achievable drawing depth for different drawing ratios after austenitization at 1050 °C for 300 and subsequent forming begin at 900 °C with a constant flange gap of 2.5 mm for the X12Cr13 (<b>a</b>), X30Cr13 (<b>b</b>) and X46Cr13 (<b>c</b>) alloys.</p>
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<p>Mean hardness HV1 and standard deviation of the cup cross section for thermomechanical treatment after initial austenitization at 1050 °C/300 s or 1150 °C/300 s and forming at 700 °C, 800 °C and 900 °C for the X12Cr13 (<b>a</b>), X30Cr13 (<b>b</b>) and X46Cr13 (<b>c</b>) alloys.</p>
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<p>Mean hardness HV1 and standard deviation of the cup cross section for thermomechanical treatment after initial austenitization at 1150 °C for 120 s or 300 s and forming at 700 °C, 800 °C and 900 °C for the X12Cr13 (<b>a</b>), X30Cr13 (<b>b</b>) and X46Cr13 (<b>c</b>) alloys.</p>
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<p>FE-simulation for the distribution of the plastic strain in a thermomechanically treated cup of X46Cr13 after austenitization at 1050 °C for 300 s and subsequent start of forming at 900 °C.</p>
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<p>FE-simulated distribution of the contact pressure between tool and workpiece during forming of the cup of X46Cr13 after austenitization at 1050 °C for 300 s and subsequent start of forming at 900 °C.</p>
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<p>Temperature–plastic strain vs. Time diagram for X46Cr13 alloy after initial austenitization at 1050 °C and immediate transfer in the tool in P1 and P2 according to <a href="#jmmp-04-00122-f012" class="html-fig">Figure 12</a> and <a href="#jmmp-04-00122-f013" class="html-fig">Figure 13</a>.</p>
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17 pages, 7550 KiB  
Article
Research on Tool Wear Based on 3D FEM Simulation for Milling Process
by Zhibo Liu, Caixu Yue, Xiaochen Li, Xianli Liu, Steven Y. Liang and Lihui Wang
J. Manuf. Mater. Process. 2020, 4(4), 121; https://doi.org/10.3390/jmmp4040121 - 16 Dec 2020
Cited by 14 | Viewed by 4010
Abstract
In the process of metal cutting, the anti-wear performance of the tool determines the life of the tool and affects the surface quality of the workpiece. The finite element simulation method can directly show the tool wear state and morphology, but due to [...] Read more.
In the process of metal cutting, the anti-wear performance of the tool determines the life of the tool and affects the surface quality of the workpiece. The finite element simulation method can directly show the tool wear state and morphology, but due to the limitations of the simulation time and complex boundary conditions, it has not been commonly used in tool life prediction. Based on this, a tool wear model was established on the platform of a finite element simulation software for the cutting process of titanium alloy TC4 by end milling. The key technique is to embed different types of tool wear models into the finite element model in combination with the consequent development technology. The effectiveness of the tool wear model was validated by comparing the experimental results with the simulation results. At the same time, in order to quickly predict the tool life, an empirical prediction formula of tool wear was established, and the change course of tool wear under time change was obtained. Full article
(This article belongs to the Special Issue Tool Wear Prediction in Manufacturing)
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<p>Flow chart of abrasion simulation.</p>
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<p>Temperature-related friction model (<b>a</b>) Stress distribution of tool-cuttings contact surface (<b>b</b>) Relationship between friction coefficient and temperature.</p>
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<p>Finite element simulation model.</p>
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<p>Schematic diagram of node displacement; (<b>a</b>) tetrahedron element (<b>b</b>) node displacement element (<b>c</b>) element of negative volume.</p>
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<p>Time-varying curve of tool abrasion.</p>
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<p>Relationship between tool abrasion mechanism and temperature.</p>
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<p>Schematic diagram of diffusion abrasion of the milling cutter flank surface.</p>
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<p>Schematic diagram of tool abrasion type at different temperatures.</p>
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<p>Milling processing test site.</p>
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<p>Experimental measurement results.</p>
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<p>Simulation cloud diagram for cutting edge into workpiece.</p>
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<p>Temperature of the cutting edge after stabilization.</p>
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<p>Cloud diagram of tool abrasion loss (unit: mm/10 s).</p>
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<p>Comparison of abrasion VB between simulation and experiment for milling cutter flank surface.</p>
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13 pages, 3543 KiB  
Article
Influence of Softening Mechanisms on Base Materials Plastic Behaviour and Defects Formation in Friction Stir Lap Welding
by Sree Sabari, Ivan Galvão, Carlos Leitão and Dulce Maria Rodrigues
J. Manuf. Mater. Process. 2020, 4(4), 120; https://doi.org/10.3390/jmmp4040120 - 13 Dec 2020
Cited by 4 | Viewed by 2423
Abstract
The AA6082-T6 and AA5754-H22 aluminium alloys were selected as the base materials to fabricate similar and dissimilar friction stir lap welds. Three lap configurations, AA6082/AA5754, AA5754/AA6082 and AA6082/AA6082, were produced using three pin profiles and tested to analyse the role of the plastic [...] Read more.
The AA6082-T6 and AA5754-H22 aluminium alloys were selected as the base materials to fabricate similar and dissimilar friction stir lap welds. Three lap configurations, AA6082/AA5754, AA5754/AA6082 and AA6082/AA6082, were produced using three pin profiles and tested to analyse the role of the plastic behaviours of the base materials on the welding conditions. The macrostructural characterisation was carried out to understand the material flow response and hook defect formation. The mechanical characterisation of the joints was done by microhardness and lap tensile shear testing. The finite element analysis and phase simulation were conducted to predict the phase dissolution temperatures and the softening kinetics. The welding torque and axial forces registered were analysed to quantify differences in the alloy’s flowability during welding. The analysis of the welding machine outputs enabled to conclude that higher axial forces were registered when the AA5754 alloy was placed at the top of the dissimilar lap joint, showing that the non-heat-treatable alloy has lower flowability than the heat-treatable alloy. These results were associated with the flow-softening of the AA6082 alloy in plastic deformation at high temperatures. The coupled experimental and numerical analysis revealed that the plastic behaviour of the base materials strongly influenced the material flow and, in this way, the hook defect formation and the shear tensile properties of the welds. Full article
(This article belongs to the Special Issue Friction Stir Welding and Related Technologies)
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<p>FSW tools used to produce the welds: (<b>a</b>) CL6, (<b>b</b>) CN6 and (<b>c</b>) CN8. CN and CL for the conical and cylindrical pin geometry.</p>
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<p>Loading modes in lap tensile–shear testing: (<b>a</b>) advancing side (AS) and (<b>b</b>) retreating side (RS).</p>
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<p>Model geometry and mesh discretisation: (<b>a</b>) workpiece and (<b>b</b>) tool.</p>
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<p>Transverse cross-section of the welds: (<b>a</b>) S6, (<b>b</b>) D65, (<b>c</b>) D56 macrographs and (<b>d</b>) D56 micrograph.</p>
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<p>NML values of the welds produced with the tools: (<b>a</b>) CN6, (<b>b</b>) CL6, (<b>c</b>) CN8.</p>
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<p>Von Mises strain maps at the maximum load for the welds produced with the CN8 tool.</p>
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<p>Microhardness profiles registered along the transverse cross-section of the welds: (<b>a</b>) S6, (<b>b</b>) D65 and (<b>c</b>) D56.</p>
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<p>FSW machine output parameters: (<b>a</b>) torque and (<b>b</b>) axial load.</p>
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<p>Temperature distribution in the transverse and the longitudinal cross-sections of the welds.</p>
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<p>Phase dissolution curves for the AA6082 aluminium alloy.</p>
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13 pages, 10711 KiB  
Communication
Laser Powder Bed Fusion with Intentionally-Seeded Porosity for Prototyping of Powder Metallurgy Parts
by Morgan Letenneur, Pete Imbrogno, Amin Molavi-Kakhki and Vladimir Brailovski
J. Manuf. Mater. Process. 2020, 4(4), 119; https://doi.org/10.3390/jmmp4040119 - 11 Dec 2020
Cited by 5 | Viewed by 3226
Abstract
Laser powder bed fusion (LPBF) additive manufacturing technology was used to produce functional prototypes of powder metallurgy (PM) components from high carbon content, iron-based water-atomized powders. The melt pool modeling and design of experiment approaches were combined in order to determine the LPBF [...] Read more.
Laser powder bed fusion (LPBF) additive manufacturing technology was used to produce functional prototypes of powder metallurgy (PM) components from high carbon content, iron-based water-atomized powders. The melt pool modeling and design of experiment approaches were combined in order to determine the LPBF operation window allowing to print parts with components similar to the PM in terms of density, microstructure and mechanical properties. The size, morphology and distribution of processing-induced pores were evaluated using computed tomography, while a microstructure analysis was carried out using X-ray diffraction and scanning electron microscopy, and the mechanical properties were evaluated using tensile and unnotched Charpy testing. It was demonstrated that LPBF technology could effectively be used for the just-in-time manufacture of high-fidelity functional prototypes of PM parts from iron-based powders. Full article
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<p>Density processing maps: (<b>A</b>) initial processing map and (<b>B</b>) adjusted processing map; positions of 25 calibration specimens are indicated on both maps; two zones corresponding to a target relative density of ~90% are indicated on the adjusted processing map; (<b>C</b>) discrepancy between the predicted and measured densities before (white dots) and after (black dots) the calibration process.</p>
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<p>Calibrated density processing maps: (<b>A</b>) unheated and (<b>B</b>) heated (200 °C) build plates; Specimens 1–4 correspond to a target density of ~90%; Specimen 5 corresponds to a ≥99.9% reference density.</p>
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<p>Building plate with printed specimens.</p>
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<p>Specimens geometry, (<b>A</b>) tensile test specimen [<a href="#B18-jmmp-04-00119" class="html-bibr">18</a>] and (<b>B</b>) unnotched Charpy impact specimen [<a href="#B19-jmmp-04-00119" class="html-bibr">19</a>].</p>
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<p>PSD of the diffusion-bonded/diffusion-alloyed FC-0208 powder.</p>
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<p>SEM micrographs of the water-atomized diffusion-bonded/diffusion-alloyed FC-0208 powders (<b>A</b>) 250× and (<b>B</b>) 1000×.</p>
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<p>2D images extracted from the CT scans: (<b>A</b>) AM (porosity 8.3%); (<b>B</b>) PM1 (porosity 8.0%) and (<b>C</b>) PM2 (porosity 8.9%); colors are added for better visualization only.</p>
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<p>Porosity analysis: (<b>A</b>) equivalent diameter and (<b>B</b>) aspect ratio.</p>
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<p>SEM images of internal porosity. (<b>A</b>) AM, (<b>B</b>) PM1 and (<b>C</b>) PM2.</p>
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<p>XRD diffractograms of the AM and PM specimens.</p>
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<p>EBSD images of the (<b>A</b>) AM, (<b>B</b>) PM1 and (<b>C</b>) PM2 specimens.</p>
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<p>Comparison of the mechanical properties of the AM and PM specimens, I for PM1 and, II for PM2.</p>
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19 pages, 14161 KiB  
Article
Probing Magnetic Pulse Welding of Thin-Walled Tubes
by Koen Faes, Rishabh Shotri and Amitava De
J. Manuf. Mater. Process. 2020, 4(4), 118; https://doi.org/10.3390/jmmp4040118 - 11 Dec 2020
Cited by 14 | Viewed by 3714
Abstract
Magnetic pulse welding is a solid-state joining technology, based on the use of electromagnetic forces to deform and to weld workpieces. Since no external heat sources are used during the magnetic pulse welding process, it offers important advantages for the joining of dissimilar [...] Read more.
Magnetic pulse welding is a solid-state joining technology, based on the use of electromagnetic forces to deform and to weld workpieces. Since no external heat sources are used during the magnetic pulse welding process, it offers important advantages for the joining of dissimilar material combinations. Although magnetic pulse welding has emerged as a novel technique to join metallic tubes, the dimensional consistency of the joint assembly due to the strong impact of the flyer tube onto the target tube and the resulting plastic deformation is a major concern. Often, an internal support inside the target tube is considered as a solution to improve the stiffness of the joint assembly. A detailed investigation of magnetic pulse welding of Cu-DHP flyer tubes and 11SMnPb30 steel target tubes is performed, with and without an internal support inside the target tubes, and using a range of experimental conditions. The influence of the key process conditions on the evolution of the joint between the tubes with progress in time has been determined using experimental investigations and numerical modelling. As the process is extremely fast, real-time monitoring of the process conditions and evolution of important responses such as impact velocity and angle, and collision velocity, which determine the formation of a metallic bond, is impossible. Therefore, an integrated approach using a computational model using a finite-element method is developed to predict the progress of the impact of the flyer onto the target, the resulting flyer impact velocity and angle, the collision velocity between the flyer and the target, and the evolution of the welded joint, which are usually impossible to measure using experimental observations. Full article
(This article belongs to the Special Issue Impulse-Based Manufacturing Technologies)
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<p>Schematic layout of magnetic pulse welding (MPW) set-up for joining of tubes.</p>
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<p>Schematic representation of the coil-tube assembly and solution domain.</p>
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<p>Actual arrangement of multi-turn bitter coil and field shaper with the collimator probe (yellow) of the photon Doppler velocimetry (PDV) setup coming out of the field shaper.</p>
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<p>Schematic representation of the tubular internal support used in the experiments with flyer tube diameter d<sub>g</sub> = 22.22 mm and target tube diameter d<sub>h</sub> = 16.44 to 18.44 mm.</p>
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<p>(<b>a</b>) Typical welded assembly and (<b>b</b>) cross-section in the as-welded condition with flyer tube diameter d<sub>g</sub> = 22.22 mm and target tube diameter d<sub>h</sub> = 16.44 to 18.44 mm.</p>
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<p>Macroscopic view of the longitudinal joint cross-section with SEM backscattered images at two random locations along the welded length, showing a slightly wavy interface profile for a weld made with a polyurethane internal support. Conditions for this welded sample: discharge energy = 14 kJ, standoff distance = 1 mm, flyer tube diameter and wall thickness = 22.22 and 0.89 mm, target tube diameter and wall thickness = 18.44 and 1 mm.</p>
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<p>Experimentally measured and analytically estimated nature of the discharge current, and numerically computed EM force for an applied energy of (<b>a</b>) 14 kJ and (<b>b</b>) 16 kJ.</p>
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<p>Numerically computed distribution of the maximum (<b>a</b>) EM field over the field shaper-tube assembly, and (<b>b</b>) EM pressure over the flyer tube for an applied energy of 14 kJ.</p>
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<p>Computed results of the progressive impact and plastic deformation of the tube assembly at the time instants of (<b>a</b>) 7 µs, (<b>b</b>) 9 µs, (<b>c</b>) 11 µs, (<b>d</b>) 17 µs, (<b>e</b>) 21 µs and (<b>f</b>) 26 µs for a discharge energy of 14 kJ and with no internal support inside the target tube. (Initial conditions: wall thicknesses of flyer = 0.89 mm and of target = 1 mm; standoff distance between flyer and target = 1 mm; overlapping length between field shaper and flyer, L<sub>w</sub> = 8 mm and free length of the flyer tube, L<sub>o</sub> = 15 mm).</p>
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<p>Computed results of the progressive impact and plastic deformation of the tube assembly at the time instants of (<b>a</b>) 9 µs, (<b>b</b>) 11 µs, (<b>c</b>) 15 µs, (<b>d</b>) 17 µs, (<b>e</b>) 21 µs and (<b>f</b>) 26 µs for an applied discharge energy of 14 kJ and with a polyurethane internal support for the target tube. (Initial conditions: wall thicknesses of the flyer = 0.89 mm and of the target = 1 mm; standoff distance between the flyer and the target = 1 mm; overlapping width between the field shaper and the flyer, L<sub>w</sub> = 8 mm and free length of the flyer tube, L<sub>o</sub> = 15 mm).</p>
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<p>Experimentally observed and computationally evaluated flyer-target joint cross-sections for a discharge energy of 14 kJ (<b>a</b>–<b>d</b>) and 16 kJ (<b>e</b>–<b>h</b>), with a polyurethane internal support inside the target tube. (Initial conditions: flyer-target standoff distance = 1 mm (<b>a</b>,<b>b</b>,<b>e</b>,<b>f</b>) and 2 mm (<b>c</b>,<b>d</b>,<b>g</b>,<b>h</b>); flyer tube: diameter = 22.22 mm, wall thicknesses = 0.89 mm; target tube: wall thicknesses = 1 mm; diameter = 18.44 mm (standoff distance = 1 mm), 16.44 mm (standoff distance = 2 mm)).</p>
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<p>Experimentally observed and computationally estimated flyer-target joint cross-sections with a polyurethane internal support (<b>a</b>,<b>b</b>), and without any internal support (<b>c</b>–<b>f</b>) for the target tube. (Initial conditions: discharge energy: 16 kJ (<b>a</b>,<b>b</b>,<b>e</b>,<b>f</b>), 14 kJ (<b>c</b>,<b>d</b>); flyer: diameter = 22.22 mm, wall thicknesses = 0.89 mm; and target: diameter = 18.44 mm, wall thicknesses = 1 mm (<b>a</b>–<b>d</b>), 2 mm (<b>e</b>,<b>f</b>); standoff distance = 1 mm).</p>
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<p>Computed values of the flyer-target contact length, the flyer impact velocity and angle and the collision velocity as a function of time, for an applied discharge energy of 14 kJ with a polyurethane internal support of the target tube. (Initial conditions: flyer: diameter = 22.22 mm, wall thicknesses = 0.89 mm; and target: diameter = 18.44 mm, wall thicknesses = 1 mm; standoff distance between the flyer and the target = 1 mm (<b>a</b>,<b>c</b>) and 2 mm (<b>b</b>,<b>d</b>)).</p>
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<p>B-H curve used to assign magnetic permeability of 11SMnPb30 steel.</p>
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19 pages, 49563 KiB  
Article
Passive Chatter Suppression of Thin-Walled Parts by Means of High-Damping Lattice Structures Obtained from Selective Laser Melting
by Federico Scalzo, Giovanni Totis, Emanuele Vaglio and Marco Sortino
J. Manuf. Mater. Process. 2020, 4(4), 117; https://doi.org/10.3390/jmmp4040117 - 10 Dec 2020
Cited by 14 | Viewed by 3479
Abstract
Chatter vibrations arising during machining operations are detrimental for cutting process performance, since they may cause poor surface quality of the machined part and severe damages to machine tool elements. Passive approaches for chatter suppression are based on the integration of special mechanical [...] Read more.
Chatter vibrations arising during machining operations are detrimental for cutting process performance, since they may cause poor surface quality of the machined part and severe damages to machine tool elements. Passive approaches for chatter suppression are based on the integration of special mechanical components with high-damping properties within the machining system. They represent a good solution to this problem thanks to their intrinsic simplicity. Recently, the application of metallic lattice structures inside 3D printed parts obtained from the Selective Laser Melting technology have proven superior damping properties with respect to the same full density material. Here, this idea is further explored by considering the novel configuration where the unmelted powder grains are retained inside the lattice structure by an external shell, acting as a multiplicity of microscopic mechanical dampers. This concept is applied for passive chatter suppression of thin-walled parts that are of particular relevance for industry. Preliminary experimental investigation was first carried out on simple beam-like specimens, and then on thin-walled benchmarks that were identified through modal analysis and tested under real cutting conditions. The main conclusion is that the novel proposed configuration (lattice plus unmelted powder) has higher damping properties with respect to the full density and lattice alternatives. Accordingly, it may be successfully applied for passive chatter suppression in real machining operations. Full article
(This article belongs to the Special Issue Machine Tool Dynamics)
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<p>Specimen design and SDOF model: longitudinal section view of the beam-like specimen under linear static FEA (<b>A</b>) and under modal FEA (<b>B</b>); equivalent single harmonic oscillator model (<b>C</b>).</p>
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<p>SLM-manufactured 316L specimens: first (<b>left</b>) and second (<b>right</b>) replicates.</p>
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<p>Images of the three replicates of lattice structure type B acquired by a digital microscope, for quality and dimensional inspection.</p>
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<p>Identification of the global dynamic behavior of the lattice structures: experimental setup for pulse testing.</p>
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<p>Specimens’ modal parameters.</p>
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<p>Blade-like benchmark geometry: dimensioned orthogonal view (<b>A</b>) and isometric view of the raw part after 3D printing (<b>B</b>).</p>
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<p>Blade like support mesh, constraints, and loads.</p>
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<p>Blade like supports CAD models.</p>
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<p>SLM 3D printed supports: reference (<b>A</b>), lattice (<b>B</b>), and lattice + powder (<b>C</b>).</p>
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<p>Experimental setup used for modal analysis (<b>a</b>) and chatter tests (<b>b</b>).</p>
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<p>Blade dynamic compliance inspected at node 3. The lower resonance peaks of the blade embedding lattice structures and powder are visible in the enlarged views in the bottom of the figure.</p>
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<p>Dynamic behavior of blade top edge derived from modal analysis: bending compliance (<b>a</b>) and torsional compliance (<b>b</b>). Dynamometer’s transmissibilities along the <math display="inline"><semantics> <msub> <mi>F</mi> <mi>y</mi> </msub> </semantics></math> (<b>c</b>) and <math display="inline"><semantics> <msub> <mi>M</mi> <mi>z</mi> </msub> </semantics></math> (<b>d</b>) directions. Dynamic relation between the bending vibration <math display="inline"><semantics> <msub> <mi>u</mi> <mi>b</mi> </msub> </semantics></math> and the measured feed perpendicular force <math display="inline"><semantics> <msub> <mi>F</mi> <mrow> <mi>y</mi> <mo>,</mo> <mi>d</mi> <mi>y</mi> <mi>n</mi> </mrow> </msub> </semantics></math> (<b>e</b>). Dynamic relation between the torsional vibration <math display="inline"><semantics> <msub> <mi>u</mi> <mi>t</mi> </msub> </semantics></math> (evaluated at blade corner—node 3) and the measured torque <math display="inline"><semantics> <msub> <mi>M</mi> <mrow> <mi>z</mi> <mo>,</mo> <mi>d</mi> <mi>y</mi> <mi>n</mi> </mrow> </msub> </semantics></math> acting on the workpiece with respect to the blade vertical axis of symmetry (<b>f</b>).</p>
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<p>Comparison between experimental and predicted stability lobes, when adopting the full density blade (<b>top</b>) the blade with lattice structure (<b>middle</b>) and the blade embedding both lattice structure and unmelted powder (<b>bottom</b>).</p>
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<p>Behavior in time and frequency domain of blade tip vibrations under flip chatter type, dominated by the first bending vibration mode. Blade type: lattice (without powder). Cutting parameters: <math display="inline"><semantics> <mrow> <mi>n</mi> <mo>=</mo> </mrow> </semantics></math> 10,250 rpm, <math display="inline"><semantics> <mrow> <msub> <mi>a</mi> <mi>p</mi> </msub> <mo>=</mo> <mn>0.5</mn> </mrow> </semantics></math> mm. Blade vibrations are derived from dynamometer signals. TPE = tooth pass excitation harmonics.</p>
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<p>Behavior in time and frequency domain of blade tip vibrations under flip chatter type, dominated by the first torsional vibration mode. Blade type: lattice filled with powder. Cutting parameters: <math display="inline"><semantics> <mrow> <mi>n</mi> <mo>=</mo> </mrow> </semantics></math> 13,500 rpm, <math display="inline"><semantics> <mrow> <msub> <mi>a</mi> <mi>p</mi> </msub> <mo>=</mo> <mn>4</mn> </mrow> </semantics></math> mm. Blade vibrations are derived from dynamometer signals. TPE = tooth pass excitation harmonics.</p>
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12 pages, 4428 KiB  
Article
A Rapid Throughput System for Shock and Impact Characterization: Design and Examples in Compaction, Spallation, and Impact Welding
by K. Sajun Prasad, Yu Mao, Anupam Vivek, Stephen R. Niezgoda and Glenn S. Daehn
J. Manuf. Mater. Process. 2020, 4(4), 116; https://doi.org/10.3390/jmmp4040116 - 10 Dec 2020
Cited by 6 | Viewed by 3446
Abstract
Many important physical phenomena are governed by intense mechanical shock and impulse. These can be used in material processing and manufacturing. Examples include the compaction or shearing of materials in ballistic, meteor, or other impacts, spallation in armor and impact to induce phase [...] Read more.
Many important physical phenomena are governed by intense mechanical shock and impulse. These can be used in material processing and manufacturing. Examples include the compaction or shearing of materials in ballistic, meteor, or other impacts, spallation in armor and impact to induce phase and residual stress changes. The traditional methods for measuring very high strain rate behavior usually include gas-guns that accelerate flyers up to km/s speeds over a distance of meters. The throughput of such experiments is usually limited to a few experiments per day and the equipment is usually large, requiring specialized laboratories. Here, a much more compact method based on the Vaporizing Foil Actuator (VFA) is used that can accelerate flyers to over 1 km/s over a few mm of travel is proposed for high throughput testing in a compact system. A system with this primary driver coupled with Photonic Doppler Velocimetry (PDV) is demonstrated to give insightful data in powder compaction allowing measurements of shock speed, spall testing giving fast and reasonable estimates of spall strength, and impact welding providing interface microstructure as a function of impact angle and speed. The essential features of the system are outlined, and it is noted that this approach can be extended to other dynamic tests as well. Full article
(This article belongs to the Special Issue Impulse-Based Manufacturing Technologies)
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<p>(<b>a</b>) A rendered CAD-model schematic and (<b>b</b>) actual photo of the chamber.</p>
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<p>A schematic showing: (<b>a</b>) the experimental setup for the measurement of projectile velocity using the Photonic Doppler Velocimetry (PDV) probe, (<b>b</b>) powder compaction of commercial pure titanium (CP-Ti), (<b>c</b>) spalling of copper (Cu110) plate, and (<b>d</b>) 20° inclined collision welding between copper (Cu110) and steel (AISI 1018).</p>
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<p>(<b>a</b>) Time-based evolution of voltage, current and velocity using an aluminum projectile with a 10 mm length, and (<b>b</b>) velocity comparison with different projectile configurations.</p>
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<p>Graph showing the comparison of projectile velocity using lubrication and without lubrication for 5 mm aluminum and composite projectiles.</p>
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<p>(<b>a</b>) Powder compaction results in terms of compact height (mm), relative density (kg/m<sup>3</sup>), and microhardness (HV) and (<b>b</b>) flyer and free surface velocity for estimation of shock velocity.</p>
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<p>(<b>a</b>) Copper target showing large spalled top surface with one piece along with several smaller shards, and (<b>b</b>) velocity traces of composite projectile and copper free surface near shock wave breakout.</p>
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<p>(<b>a</b>) Copper target grooved with 20° inclination, (<b>b</b>) steel welded to copper target, (<b>c</b>) sectional view of the welded part, and (<b>d</b>) optical image showing complete welding profile.</p>
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12 pages, 5944 KiB  
Article
Hybrid Additive Manufacturing of Collector Coins
by João P. M. Pragana, Stephan Rosenthal, Ivo M. F. Bragança, Carlos M. A. Silva, A. Erman Tekkaya and Paulo A. F. Martins
J. Manuf. Mater. Process. 2020, 4(4), 115; https://doi.org/10.3390/jmmp4040115 - 9 Dec 2020
Cited by 7 | Viewed by 3797
Abstract
The objective of this paper is to present a new hybrid additive manufacturing route for fabricating collector coins with complex, intricate contoured holes. The new manufacturing route combines metal deposition by additive manufacturing with metal cutting and forming, and its application is illustrated [...] Read more.
The objective of this paper is to present a new hybrid additive manufacturing route for fabricating collector coins with complex, intricate contoured holes. The new manufacturing route combines metal deposition by additive manufacturing with metal cutting and forming, and its application is illustrated with an example consisting of a prototype coin made from stainless steel AISI 316L. Experimentation and finite element analysis of the coin minting operation with the in-house computer program i-form show that the blanks produced by additive manufacturing and metal cutting can withstand the high compressive pressures that are attained during the embossing and impressing of lettering and other reliefs on the coin surfaces. The presentation allows concluding that hybrid additive manufacturing opens the way to the production of innovative collector coins with geometric features that are radically different from those that are currently available in the market. Full article
(This article belongs to the Special Issue Metal Forming and Joining)
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Graphical abstract

Graphical abstract
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<p>Extended classification of hybrid manufacturing (HM) to include hybrid additive manufacturing (HAM) routes (adapted from Pragana et al. [<a href="#B2-jmmp-04-00115" class="html-bibr">2</a>]).</p>
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<p>New hybrid additive manufacturing (HAM) route to produce collector coins showing the integration of (<b>a</b>) laser powder bed fusion with (<b>b</b>) wire electro-discharge machining (wire-EDM), (<b>c</b>) polishing and (<b>d</b>) coin minting. A prototype coin with details of its major geometrical features is shown in (<b>e</b>), where the label “A” refers to very small holes, “B” to tears with very small angles, “C” to overhang corners and “D” to small bridges between the center and the outer regions of the blanks.</p>
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<p>Deposition strategy utilized in the fabrication of the blanks and cylindrical test specimens of AISI 316L by laser powder bed fusion.</p>
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<p>Photographs of the additively manufactured blanks: (<b>a</b>) the constructed cylinder’s end; (<b>b</b>) the blank sliced from the constructed cylinder by wire-EDM; (<b>c</b>) the blank sliced from the constructed cylinder by wire-EDM and polished.</p>
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<p>(<b>a</b>) Press-tool system utilized in the coin minting experiments; (<b>b</b>) details of the upper and lower dies.</p>
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<p>(<b>a</b>) Finite element model at the beginning of die stroke; (<b>b</b>) top view and detail of the initial mesh; (<b>c</b>) computed geometry and photograph of the prototype coin at the end of die stroke.</p>
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<p>Coin minting of the additively manufactured blanks of AISI 316L stainless steel. (<b>a</b>) Photographs; (<b>b</b>) finite-element-predicted distribution of pressure (MPa); (<b>c</b>) finite-element-predicted distribution of relative density at 0%, 30%, 90% and 100% of the total die stroke.</p>
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<p>(<b>a</b>) Photograph and (<b>b</b>) normalized in-plane velocity <math display="inline"><semantics> <mrow> <msub> <mi>v</mi> <mrow> <mi>x</mi> <mi>y</mi> </mrow> </msub> <mo>/</mo> <mrow> <mo>|</mo> <mrow> <msub> <mi>v</mi> <mrow> <mi>d</mi> <mi>i</mi> <mi>e</mi> </mrow> </msub> </mrow> <mo>|</mo> </mrow> </mrow> </semantics></math> at 150% of the total die stroke.</p>
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<p>Finite element calculated point of application <math display="inline"><semantics> <mrow> <mrow> <mo>(</mo> <mrow> <mi>x</mi> <mo>,</mo> <mo> </mo> <mi>y</mi> </mrow> <mo>)</mo> </mrow> </mrow> </semantics></math> of the resultant vertical force at the end of coin minting in the reverse and obverse dies.</p>
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<p>Experimental and finite-element-predicted evolutions of force with die stroke during coin minting of the additively manufactured blanks made AISI 316L stainless steel.</p>
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13 pages, 11638 KiB  
Article
Optimization of Wet Grinding Conditions of Sheets Made of Stainless Steel
by Akira Mizobuchi and Atsuyoshi Tashima
J. Manuf. Mater. Process. 2020, 4(4), 114; https://doi.org/10.3390/jmmp4040114 - 7 Dec 2020
Cited by 2 | Viewed by 3111
Abstract
This study addresses the wet grinding of large stainless steel sheets, because it is difficult to subject them to dry grinding. Because stainless steel has a low thermal conductivity and a high coefficient of thermal expansion, it easily causes grinding burn and thermal [...] Read more.
This study addresses the wet grinding of large stainless steel sheets, because it is difficult to subject them to dry grinding. Because stainless steel has a low thermal conductivity and a high coefficient of thermal expansion, it easily causes grinding burn and thermal deformation while dry grinding on the wheel without applying a cooling effect. Therefore, wet grinding is a better alternative. In this study, we made several types of grinding wheels, performed the wet grinding of stainless steel sheets, and identified the wheels most suitable for the process. As such, this study developed a special accessory that could be attached to a wet grinding workpiece. The attachment can maintain constant pressure, rotational speed, and supply grinding fluid during work. A set of experiments was conducted to see how some grinding wheels subjected to some grinding conditions affected the surface roughness of a workpiece made of a stainless steel sheet (SUS 304, according to Japanese Industrial Standards: JIS). It was found that the roughness of the sheet could be minimized when a polyvinyl alcohol (PVA) grinding wheel was used as the grinding wheel and tap water was used as the grinding fluid at an attachment pressure of 0.2 MPa and a rotational speed of 150 rpm. It was shown that a surface roughness of up to 0.3 μm in terms of the arithmetic average height could be achieved if the above conditions were satisfied during wet grinding. The final surface roughness was 0.03 μm after finish polishing by buffing. Since the wet grinding of steel has yet to be studied in detail, this article will serve as a valuable reference. Full article
(This article belongs to the Special Issue Intelligent Machining and Grinding)
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<p>Developed wet grinding machine and attachment points for the grinding wheels.</p>
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<p>Magnet attachment and grinding fluid drain.</p>
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<p>Wet tabletop grinding equipment.</p>
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<p>Rockwell hardness measurements of grinding wheels.</p>
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<p>Average abrasion loss of the grinding wheel thickness after grinding.</p>
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<p>Conditions of the 180G, 400G, and 400SP wheels after machining.</p>
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<p>Loss ratio of each wheel.</p>
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<p>Surface properties of the stainless steel sheet (<b>a</b>) Before grinding (<b>b</b>) 180G (<b>c</b>) 180O (<b>d</b>) 240K (<b>e</b>) 400G (<b>f</b>) 400SP.</p>
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<p>Arithmetic average height and largest peak to valley height of the assessed profile of the steel sheet after grinding.</p>
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<p>Loss ratios for rough and semi-finish grinding.</p>
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<p>Condition of the steel sheet after grinding with the 180K–400SP and 240K–400SP combinations.</p>
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<p>Arithmetic average height of the assessed profile of the steel sheet after the semi-finish grinding.</p>
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<p>Loss ratios of the steel sheet after the semi-finish grinding.</p>
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<p>Steel sheet surface conditions.</p>
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<p>Steel sheet surface conditions.</p>
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<p>Surface condition and surface roughness when grinding with the 180K–400SP and 240K–400SP combinations.</p>
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<p>Surface condition and roughness when grinding with the 400K–400SP, 400N–400SP, and 400SP combinations.</p>
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<p>Machined surfaces under the conventional method with a flap wheel (<b>a</b>) and the proposed method with the 400SP wheel (<b>b</b>).</p>
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13 pages, 5615 KiB  
Article
Influence of the CO2 Content in Shielding Gas on the Temperature of the Shielding Gas Nozzle during GMAW Welding
by Martin Lohse, Marcus Trautmann, Uwe Füssel and Sascha Rose
J. Manuf. Mater. Process. 2020, 4(4), 113; https://doi.org/10.3390/jmmp4040113 - 4 Dec 2020
Cited by 3 | Viewed by 4135
Abstract
Gas metal arc welding torches are commonly chosen based on their current-carrying capacity. It is known that the current-carrying capacity of welding torches under CO2 is usually higher than under argon dominated shielding gases. In this publication, the extent to which this [...] Read more.
Gas metal arc welding torches are commonly chosen based on their current-carrying capacity. It is known that the current-carrying capacity of welding torches under CO2 is usually higher than under argon dominated shielding gases. In this publication, the extent to which this can be attributed to the shielding gas dependent arc radiation is investigated. For this purpose, the influence of the shielding gas on the thermal load of the shielding gas nozzle of a GMAW torch was calorimetrically measured. These experiments were carried out for four different shielding gases (argon, CO2, and two argon/CO2 mixtures). The measurements were all performed at an average current of 300 A. The welding current was set by adjusting the wire feed rate or the voltage correction. For each case, a separate set of experiments was done. It is shown that the changed arc radiation resulting from the different shielding gases has an influence on the heat input into the gas nozzle, and thus into the torch. For the same shielding gas, this influence largely correlates with the welding voltage. Full article
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<p>Specific heat and thermal conductivity of argon and carbon dioxide in comparison [<a href="#B10-jmmp-04-00113" class="html-bibr">10</a>,<a href="#B11-jmmp-04-00113" class="html-bibr">11</a>].</p>
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<p>Measured arc temperatures for a gas metal arc welding (GMAW) pulse process. Values under argon determined in [<a href="#B12-jmmp-04-00113" class="html-bibr">12</a>] for an arc 1040 ms after the start of the high current phase and 1.7 mm above the workpiece. Values for 82% argon/18% CO<sub>2</sub> and CO<sub>2</sub> determined in [<a href="#B13-jmmp-04-00113" class="html-bibr">13</a>] for an arc 980 ms after the start of the high current phase approximately 1.5 mm above the workpiece. The welding current at the time of measurement was about 420 A for argon, about 250 A for 82% argon/18% CO<sub>2</sub>, and about 330 A for CO<sub>2</sub>.</p>
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<p>Net emission coefficient of argon and carbon dioxide compared. Data is taken from [<a href="#B14-jmmp-04-00113" class="html-bibr">14</a>,<a href="#B15-jmmp-04-00113" class="html-bibr">15</a>].</p>
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<p>Design of the gas nozzle cooling and current-carrying torch parts. (<b>Left</b>) principle sketch; (<b>Right</b>) design of the torch.</p>
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<p>Current and voltage for an argon shielding gas with 0%, 2.5%, 18%, and 100% CO<sub>2</sub>.</p>
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<p>Visible arc length of the examined shielding gases in qualitative comparison.</p>
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<p>Heat input into the gas nozzle for the examined shielding gases.</p>
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<p>Average heat input into the gas nozzle for the examined shielding gases with variance over the evaluated period at 300 A.</p>
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<p>Current and voltage for an argon shield gas with 0%, 2.5%, 18%, and 100% CO<sub>2</sub> content.</p>
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<p>Visible arc length of the examined shielding gases in qualitative comparison.</p>
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<p>Heat input into the gas nozzle for the examined shielding gases.</p>
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<p>Average heat input into the gas nozzle for the examined shielding gases with variance over the evaluated period.</p>
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<p>Average heat input into the gas nozzle for the examined shielding gases from the two test series.</p>
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15 pages, 14647 KiB  
Article
Improving Geometric Accuracy of 3D Printed Parts Using 3D Metrology Feedback and Mesh Morphing
by Moustapha Jadayel and Farbod Khameneifar
J. Manuf. Mater. Process. 2020, 4(4), 112; https://doi.org/10.3390/jmmp4040112 - 29 Nov 2020
Cited by 20 | Viewed by 4538
Abstract
Additive manufacturing (AM), also known as 3D printing, has gained significant interest due to the freedom it offers in creating complex-shaped and highly customized parts with little lead time. However, a current challenge of AM is the lack of geometric accuracy of fabricated [...] Read more.
Additive manufacturing (AM), also known as 3D printing, has gained significant interest due to the freedom it offers in creating complex-shaped and highly customized parts with little lead time. However, a current challenge of AM is the lack of geometric accuracy of fabricated parts. To improve the geometric accuracy of 3D printed parts, this paper presents a three-dimensional geometric compensation method that allows for eliminating systematic deviations by morphing the original surface mesh model of the part by the inverse of the systematic deviations. These systematic deviations are measured by 3D scanning multiple sacrificial printed parts and computing an average deviation vector field throughout the model. We demonstrate the necessity to filter out the random deviations from the measurement data used for compensation. Case studies demonstrate that printing the compensated mesh model based on the average deviation of five sacrificial parts produces a part with deviations about three times smaller than measured on the uncompensated parts. The deviation values of this compensated part based on the average deviation vector field are less than half of the deviation values of the compensated part based on only one sacrificial part. Full article
(This article belongs to the Special Issue Direct Digital Manufacturing with Additive Manufacturing/3D Printing)
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<p>Outline of the proposed 3D compensation.</p>
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<p>Ultimaker 3, 3D printing the part in PLA.</p>
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<p>NIST CTC 5 CAD model.</p>
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<p>3D scanning setup with ATOS Core.</p>
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<p>Scan data of the printed part.</p>
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<p>Deviation colormaps of the five original printed parts, ranges are in <math display="inline"><semantics> <mi mathvariant="sans-serif">μ</mi> </semantics></math>m.</p>
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<p>Deviation colormap of the compensated part based on part B, range is in <math display="inline"><semantics> <mi mathvariant="sans-serif">μ</mi> </semantics></math>m.</p>
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<p>Average deviation colormap of the five original printed parts, range is in <math display="inline"><semantics> <mi mathvariant="sans-serif">μ</mi> </semantics></math>m.</p>
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<p>Standard deviation colormap of the five original printed parts, range is in <math display="inline"><semantics> <mi mathvariant="sans-serif">μ</mi> </semantics></math>m.</p>
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<p>Deviation colormap of the compensated part based on the average of five parts, range is in <math display="inline"><semantics> <mi mathvariant="sans-serif">μ</mi> </semantics></math>m.</p>
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<p>Drawing of the part with the toleranced features to inspect. Unless otherwise specified, dimensions are in mm.</p>
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18 pages, 10326 KiB  
Article
The Influence of Servo Drive Control on the NC Vertical Milling Machine Dynamic Compliance
by Jan Grau, Pavel Souček and Matěj Sulitka
J. Manuf. Mater. Process. 2020, 4(4), 111; https://doi.org/10.3390/jmmp4040111 - 26 Nov 2020
Cited by 2 | Viewed by 2664
Abstract
A model Numerical Control (NC) machine tool dynamic compliance is analyzed, including the influence of its mechanical structure and position control feed drive algorithms. The dynamic model of the machine tool is divided into two main parts, which are closest to the machining [...] Read more.
A model Numerical Control (NC) machine tool dynamic compliance is analyzed, including the influence of its mechanical structure and position control feed drive algorithms. The dynamic model of the machine tool is divided into two main parts, which are closest to the machining process. First, the milling head assembly group is presented as a system of one mass oscillating in a 2D plane and 3D space. Second, the motion axes assembly group, XY cross table with linear feed drive, is presented. A square 2×2 dimension matrix of the total dynamic compliance is evaluated within the feed drive control system included. Partial elements of the mechanical structure dynamic compliance matrix of the general N×N dimension are contained in the total dynamic compliance matrix. Full article
(This article belongs to the Special Issue Machine Tool Dynamics)
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<p>Feedback regenerative principle for calculating real chip thickness.</p>
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<p>Vertical milling center MCFV 5050 LN (TAJMAC-ZPS, Zlín, Czechia).</p>
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<p>Scheme of machine tool structural parts modeled by <math display="inline"><semantics> <mrow> <msub> <mi>G</mi> <mi>S</mi> </msub> </mrow> </semantics></math> and <math display="inline"><semantics> <mrow> <msub> <mi>G</mi> <mi>R</mi> </msub> </mrow> </semantics></math> dynamic compliance.</p>
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<p>Mid-sized milling machine with vibration source (<b>a</b>) schematic top view (<b>b</b>).</p>
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<p>Dynamic compliance polar diagram at selected frequencies.</p>
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<p>Three degrees of freedom oscillation model.</p>
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<p>Direct static compliance surface (magenta) with inscribed ellipsoid of compliance.</p>
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<p>Model of the direct dynamic (blue shape) and static compliance (magenta shape, as in <a href="#jmmp-04-00111-f007" class="html-fig">Figure 7</a>).</p>
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<p>Cascade regulation with linear motor block diagram (filters are not included).</p>
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<p>N-mass system with regulation.</p>
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<p>Block diagram for system dynamic compliance evaluation.</p>
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<p>N-mass system with regulation <math display="inline"><semantics> <mrow> <msub> <mi>G</mi> <mi>R</mi> </msub> <mrow> <mo>(</mo> <mi>s</mi> <mo>)</mo> </mrow> </mrow> </semantics></math>-quadrupole scheme.</p>
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<p>Real part of spindle directional dynamic compliance.</p>
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<p>XY cross table CAD model [<a href="#B19-jmmp-04-00111" class="html-bibr">19</a>].</p>
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<p>Two-mass scheme of XY cross table.</p>
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<p>Axis X linear motor one-mass system model.</p>
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<p>Experimental measuring on the mid-sized vertical machine X axis (<b>a</b>), and mathematical simulation (<b>b</b>).</p>
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<p>Axis Y dynamic compliance <math display="inline"><semantics> <mrow> <msub> <mi>G</mi> <mrow> <mi>R</mi> <mn>11</mn> </mrow> </msub> </mrow> </semantics></math>.</p>
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<p>Reconstructed axis Y model dynamic compliance <math display="inline"><semantics> <mrow> <msub> <mi mathvariant="normal">G</mi> <mrow> <mi mathvariant="normal">R</mi> <mn>22</mn> </mrow> </msub> <mo>.</mo> </mrow> </semantics></math></p>
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<p>Real part of the table directional dynamic compliance.</p>
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<p>Real part of coupled dynamic compliance of spindle and cross table.</p>
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<p>Spindle and its model transfer function—100°.</p>
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<p>Influence of <math display="inline"><semantics> <mrow> <msub> <mi>K</mi> <mi>V</mi> </msub> </mrow> </semantics></math> constant on the real part of transfer function.</p>
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<p>Stability lobe diagram SLD diagram for various <span class="html-italic">K<sub>V</sub></span> set-up</p>
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15 pages, 10015 KiB  
Article
Process Optimization for 100 W Nanosecond Pulsed Fiber Laser Engraving of 316L Grade Stainless Steel
by Stephen D. Dondieu, Krystian L. Wlodarczyk, Paul Harrison, Adam Rosowski, Jack Gabzdyl, Robert L. Reuben and Duncan P. Hand
J. Manuf. Mater. Process. 2020, 4(4), 110; https://doi.org/10.3390/jmmp4040110 - 26 Nov 2020
Cited by 12 | Viewed by 4502
Abstract
High average power (>50 W) nanosecond pulsed fiber lasers are now routinely available owing to the demand for high throughput laser applications. However, in some applications, scale-up in average power has a detrimental effect on process quality due to laser-induced thermal accumulation in [...] Read more.
High average power (>50 W) nanosecond pulsed fiber lasers are now routinely available owing to the demand for high throughput laser applications. However, in some applications, scale-up in average power has a detrimental effect on process quality due to laser-induced thermal accumulation in the workpiece. To understand the laser–material interactions in this power regime, and how best to optimize process performance and quality, we investigated the influence of laser parameters such as pulse duration, energy dose (i.e., total energy deposited per unit area), and pulse repetition frequency (PRF) on engraving 316L stainless steel. Two different laser beam scanning strategies, namely, sequential method (SM) and interlacing method (IM), were examined. For each set of parameters, the material removal rate (MRR) and average surface roughness (Sa) were measured using an Alicona 3D surface profilometer. A phenomenological model has been used to help identify the best combination of laser parameters for engraving. Specifically, this study has found that (i) the model serves as a quick way to streamline parameters for area engraving (ii) increasing the pulse duration and energy dose at certain PRF results in a high MRR, albeit with an associated increase in Sa, and (iii) the IM offers 84% reduction in surface roughness at a higher MRR compared to SM. Ultimately, high quality at high throughput engraving is demonstrated using optimized process parameters. Full article
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<p>(<b>a</b>) Measured temporal profiles of some selected waveforms shortlisted for the experimental work. WFM 23 (17 ns), WFM 14 (60 ns), WFM 5 (150 ns), WFM 0 (280 ns), WFM 28 (380 ns), and WFM 31 (500 ns). (<b>b</b>) Temporal profile as a function of pulse repetition frequency (PRF) for WFM 0.</p>
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<p>Flowchart of the experimental protocol.</p>
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<p>(<b>a</b>) Surface height map of lines machined with 280 ns pulses at different line energy doses (<math display="inline"><semantics> <mrow> <mi>E</mi> <msub> <mi>D</mi> <mi>L</mi> </msub> </mrow> </semantics></math>). (<b>b</b>–<b>d</b>) Extracted 3D profiles of the highlighted region: (b) full profile, (<b>c</b>) extracted groove profile (material removed), and (d) extracted burr profile (redeposited material) [μm].</p>
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<p>Schematic representation of (<b>a</b>) bidirectional sequential method (SM) and (<b>b</b>–<b>f</b>) bidirectional interlacing method (IM). (<b>b</b>) IM with one line skip (∆IL = 2 <math display="inline"><semantics> <mrow> <mo>Δ</mo> <mi>H</mi> </mrow> </semantics></math>), (<b>c</b>) IM with 2 line skips (∆IL = 3 <math display="inline"><semantics> <mrow> <mo>Δ</mo> <mi>H</mi> </mrow> </semantics></math>), (<b>d</b>) IM with 3 line skips (∆IL = 4 <math display="inline"><semantics> <mrow> <mo>Δ</mo> <mi>H</mi> </mrow> </semantics></math>), (<b>e</b>) IM with 4 line skips (∆IL = 4 <math display="inline"><semantics> <mrow> <mo> </mo> <mo>Δ</mo> <mi>H</mi> </mrow> </semantics></math>), and (<b>f</b>) IM with 5 line skips (∆IL = 5 <math display="inline"><semantics> <mrow> <mo>Δ</mo> <mi>H</mi> </mrow> </semantics></math>). In all these scanning modes, the total process time is identical. For image clarity, the hatch distance was chosen at half the laser spot diameter in this illustration.</p>
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<p>(<b>a</b>) 3D profiles of various classes of groove produced during the single-line machining and the (<b>b</b>) corresponding cross-sectional profiles.</p>
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<p>(<b>a</b>) Extracted volume of groove and (<b>b</b>) extracted volume of burr produced as a function of line energy dose (<math display="inline"><semantics> <mrow> <mi>E</mi> <msub> <mi>D</mi> <mi>L</mi> </msub> </mrow> </semantics></math>) for different pulse durations at PRF<sub>0</sub>. (<b>c</b>) Cross section of grooves produced at 60 ns and 500 ns pulse durations for different energy doses. The parameter combinations highlighted in red have been excluded from further experiments as the quality of machining is poor.</p>
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<p>(<b>a</b>) Volume of groove; (<b>b</b>) volume of the burr as a function of PRF at a constant <math display="inline"><semantics> <mrow> <mi>E</mi> <msub> <mi>D</mi> <mi>L</mi> </msub> </mrow> </semantics></math> of 0.09 J/mm; and (<b>c</b>) cross-sectional view for the influence of change in PRFs at 280 ns, 380 ns, and 500 ns.</p>
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<p>(<b>a</b>) Photograph comparing sequential method (SM) to interlacing method (IM). (<b>b</b>) Surface morphology for SM. (<b>c</b>–<b>g</b>) Surface morphology at different interlacing distances (∆IL), produced at a scan speed of 1900 mm/s, 280 ns and <math display="inline"><semantics> <mrow> <mi>E</mi> <msub> <mi>D</mi> <mi>A</mi> </msub> </mrow> </semantics></math>= 4.2 J/mm<sup>2</sup>.</p>
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<p>Cross-sectional profile highlighting the difference between (<b>a</b>) SM at material removal rate (MRR) = 14 mm<sup>3</sup>/min, S<sub>a</sub> = 32 µm and (<b>b</b>) IM at MRR = 15 mm<sup>3</sup>/min, S<sub>a</sub> = 5 µm processed at 5.3 J/mm<sup>2</sup> at 280 ns.</p>
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<p>(<b>a</b>) MRR and (<b>b</b>) S<sub>a</sub> as a function of area energy dose (<math display="inline"><semantics> <mrow> <mi>E</mi> <msub> <mi>D</mi> <mi>A</mi> </msub> </mrow> </semantics></math>) for different pulse durations. The highlighted region in panel (<b>a</b>) excludes 60 ns (&gt;2.7 J/mm<sup>2</sup>), and the dashed line represents a critical <math display="inline"><semantics> <mrow> <mi>E</mi> <msub> <mi>D</mi> <mi>A</mi> </msub> </mrow> </semantics></math> beyond which the surface is blackened and surface quality deteriorates significantly.</p>
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<p>(<b>a</b>) MRR and (<b>b</b>) S<sub>a</sub> as a function of PRF and τ at a constant <math display="inline"><semantics> <mrow> <mi>E</mi> <msub> <mi>D</mi> <mi>A</mi> </msub> </mrow> </semantics></math> of 4.2 J/mm<sup>2</sup>.</p>
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<p>SEM micrographs of the surface topology at different PRFs processed at <math display="inline"><semantics> <mrow> <mi>E</mi> <msub> <mi>D</mi> <mi>A</mi> </msub> </mrow> </semantics></math> of 4.2 J/mm<sup>2</sup> at 280 ns.</p>
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<p>SEM micrographs of the surface morphology processed at different PRFs at <math display="inline"><semantics> <mrow> <mi>E</mi> <msub> <mi>D</mi> <mi>A</mi> </msub> </mrow> </semantics></math> of 4.2 J/mm<sup>2</sup> at 500 ns.</p>
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<p>Morphology of high-quality constant depth area engraving (<b>a</b>) 13 mm<sup>3</sup>/min MRR at 1.4 µm S<sub>a</sub> using: Engraving pass at 4.2 J/mm<sup>2</sup>, 380 ns, 175 kHz; Cleaning pass at 150 ns, 350 kHz, 3.5 J/mm<sup>2</sup> and polishing pass at 1.82 J/mm<sup>2</sup>, 500 ns, 500 kHz using IM and halftone scanning. (<b>b</b>) Inverted stepped pyramid-shaped engraving.</p>
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14 pages, 2538 KiB  
Article
Digital Twin Based Optimization of a Manufacturing Execution System to Handle High Degrees of Customer Specifications
by Andrea Barni, Dario Pietraroia, Simon Züst, Shaun West and Oliver Stoll
J. Manuf. Mater. Process. 2020, 4(4), 109; https://doi.org/10.3390/jmmp4040109 - 17 Nov 2020
Cited by 24 | Viewed by 7550
Abstract
Lean production principles have greatly contributed to the efficient and customer-oriented mass production of goods and services. A core element of lean production is the focus on cycle times and designing production controls and buffers around any bottlenecks in the system. Hence, a [...] Read more.
Lean production principles have greatly contributed to the efficient and customer-oriented mass production of goods and services. A core element of lean production is the focus on cycle times and designing production controls and buffers around any bottlenecks in the system. Hence, a production line organized by lean principles will operate in a static or at least quasi-static way. While the individualization of products is an interesting business approach, it can influence cycle times and in-time production. This work demonstrates how performance losses induced by highly variable cycle times can be recovered using a digital twin. The unit under analysis is an industrial joiner’s workshop. Due to the high variance in cycle time, the joinery fails its production target, even if all machines are below 80% usage. Using a discrete event simulation of the production line, different production strategies can be evaluated efficiently and systematically. It is successfully shown that the performance losses due to the highly variable cycle times can be compensated using a digital twin in combination with optimization strategies. This is achieved by operating the system in a non-static mode, exploiting the flexibilities within the systems. Full article
(This article belongs to the Special Issue AI Applications in Smart and Advanced Manufacturing)
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<p>PDF of the time to completion for two different levels of cycle-time variation.</p>
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<p>Principal procedure of the digital twin and data/information exchange with the physical system.</p>
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<p>Identified layout of the production process (P: process step, B: branch).</p>
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<p>Identified layout of the production area.</p>
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<p>Production schedule prior to optimization for the use-case.</p>
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<p>Optimized production schedule for the use-case.</p>
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<p>Optimized maintenance schedule for the use-case. The red square indicates the maintenance process.</p>
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20 pages, 2747 KiB  
Article
Advances in Machine Learning Detecting Changeover Processes in Cyber Physical Production Systems
by Bastian Engelmann, Simon Schmitt, Eddi Miller, Volker Bräutigam and Jan Schmitt
J. Manuf. Mater. Process. 2020, 4(4), 108; https://doi.org/10.3390/jmmp4040108 - 13 Nov 2020
Cited by 20 | Viewed by 5522
Abstract
The performance indicator, Overall Equipment Effectiveness (OEE), is one of the most important ones for production control, as it merges information of equipment usage, process yield, and product quality. The determination of the OEE is oftentimes not transparent in companies, due to the [...] Read more.
The performance indicator, Overall Equipment Effectiveness (OEE), is one of the most important ones for production control, as it merges information of equipment usage, process yield, and product quality. The determination of the OEE is oftentimes not transparent in companies, due to the heterogeneous data sources and manual interference. Furthermore, there is a difference in present guidelines to calculate the OEE. Due to a big amount of sensor data in Cyber Physical Production Systems, Machine Learning methods can be used in order to detect several elements of the OEE by a trained model. Changeover time is one crucial aspect influencing the OEE, as it adds no value to the product. Furthermore, changeover processes are fulfilled manually and vary from worker to worker. They always have their own procedure to conduct a changeover of a machine for a new product or production lot. Hence, the changeover time as well as the process itself vary. Thus, a new Machine Learning based concept for identification and characterization of machine set-up actions is presented. Here, the issue to be dealt with is the necessity of human and machine interaction to fulfill the entire machine set-up process. Because of this, the paper shows the use case in a real production scenario of a small to medium size company (SME), the derived data set, promising Machine Learning algorithms, as well as the results of the implemented Machine Learning model to classify machine set-up actions. Full article
(This article belongs to the Special Issue Cyber Physical Production Systems)
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<p>OEE in the context of Machine Learning.</p>
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<p>Milling machine and sensor setup.</p>
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<p>Data handling structure.</p>
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<p>Tested algorithms used for training.</p>
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<p>Confusion Matrix of Fine Tree Algorithm (True Positive Rates, False Negative Rates) (<b>left</b>) Confusion Matrix of RUSBoosted Tree Algorithm (True Positive Rates, False Negative Rates) (<b>right</b>).</p>
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<p>ROC-Curve of Fine Tree Algorithm with production as positive class (<b>a</b>) and changeover as positive class (<b>b</b>); ROC-Curve of RUSBoostedTree Algorithm with production as positive class (<b>c</b>); and, changeover as positive class (<b>d</b>).</p>
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<p>Exemplary RUS Boosted Tree.</p>
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16 pages, 6032 KiB  
Article
Influence of Powder Particle Morphology on the Static and Fatigue Properties of Laser Powder Bed-Fused Ti-6Al-4V Components
by Salah Eddine Brika and Vladimir Brailovski
J. Manuf. Mater. Process. 2020, 4(4), 107; https://doi.org/10.3390/jmmp4040107 - 9 Nov 2020
Cited by 6 | Viewed by 2835
Abstract
In this work, two Ti-6Al-4V powder lots were produced using two different techniques: plasma atomization and gas atomization, with the first producing more spherical particles than the second. Testing specimens were then manufactured with these powder lots using an identical set of printing [...] Read more.
In this work, two Ti-6Al-4V powder lots were produced using two different techniques: plasma atomization and gas atomization, with the first producing more spherical particles than the second. Testing specimens were then manufactured with these powder lots using an identical set of printing parameters and the same laser powder bed fusion system. Next, the porosity levels and distributions as well as the static and fatigue properties of the specimens from both powder lots were compared. Regarding the static mechanical properties, a noticeable difference was observed between the plasma-atomized powder specimens and their gas-atomized equivalents (7% greater ultimate and 4% greater yield strengths, but 3% lower elongation to failure, respectively). However, with regard to the fatigue resistance, the advantages of the plasma-atomized powder specimens in terms of their mechanical resistance were somewhat counterbalanced by the presence of pores aligned in the direction perpendicular to that of applied load. Conversely, specimens printed with the gas-atomized powder manifested a similar level of porosity, but a uniform pore distribution, which reduced the impact of the processing-induced porosity on fatigue cracks initiation and propagation. Full article
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<p>Printed specimens (dimensions in mm): (<b>a</b>) tensile and (<b>b</b>) fatigue specimens; all specimens were machined from the corresponding vertically printed blanks.</p>
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<p>(<b>a</b>,<b>b</b>) SEM micrographs of two powder lots; (<b>c</b>) cumulative particle size distributions; (<b>d</b>) particle sphericity distributions; panels (<b>c</b>,<b>d</b>) are obtained using µCT analysis.</p>
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<p>Internal defect characteristic distributions: (<b>a</b>) equivalent diameter, (<b>b</b>) aspect ratio, and (<b>c</b>) mean Feret diameter.</p>
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<p>Processing-induced pores characterization (µCT): (<b>a</b>) 2D vertical sections of the gauge regions of tensile specimens printed with two powders and (<b>b</b>) 2D horizontal and vertical sections of the gauge regions of fatigue specimens printed with two powders. Aligned pores could be seen in the tensile and fatigue specimens produced with the plasma-atomized powder.</p>
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<p>Static mechanical properties of specimens printed with two studied powder lots.</p>
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<p>S-N diagrams obtained for the two studied powder lots.</p>
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<p>Fatigue limit (stress ratio R = 0.1, runout 10<sup>7</sup> cycles,) versus ultimate tensile strength diagram: comparison of the results of this study with the literature (vertically printed specimens).</p>
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<p>Fractographic examination of specimens printed from the gas-atomized (<b>a</b>,<b>b</b>) and plasma-atomized (<b>c</b>,<b>d</b>) powders: (<b>a</b>) gas-atomized, the arrows indicating the crack initiation site; (<b>b</b>) gas-atomized, zoom-in on the origin of the crack; (<b>c</b>) plasma-atomized, aligned pores and arrows indicating the crack initiation site, (<b>d</b>) plasma-atomized, zoom in on the origin of the crack; both failed under a maximum stress of 800 MPa.</p>
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<p>Diffraction patterns and phase maps of the specimens produced using the two powder lots.</p>
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<p>EBSD orientation maps: (<b>a</b>) Gas-atomized specimen; (<b>b</b>) Plasma-atomized specimen.</p>
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21 pages, 3938 KiB  
Article
Virtual Quality Gates in Manufacturing Systems: Framework, Implementation and Potential
by Marc-André Filz, Sebastian Gellrich, Artem Turetskyy, Jacob Wessel, Christoph Herrmann and Sebastian Thiede
J. Manuf. Mater. Process. 2020, 4(4), 106; https://doi.org/10.3390/jmmp4040106 - 9 Nov 2020
Cited by 25 | Viewed by 7004
Abstract
Manufacturing companies are exposed to increased complexity and competition. To stay competitive, companies need to minimize the total cost of quality while ensuring high transparency about process–product relationships within the manufacturing system. In this context, the development of technologies such as advanced analytics [...] Read more.
Manufacturing companies are exposed to increased complexity and competition. To stay competitive, companies need to minimize the total cost of quality while ensuring high transparency about process–product relationships within the manufacturing system. In this context, the development of technologies such as advanced analytics and cyber physical production systems offer a promising approach. This paper discusses and defines essential elements of virtual quality gates in the context of manufacturing systems. To support the planning and implementation of virtual quality gates, a morphological box is developed which can be used to identify and derive an individual approach for a virtual quality gate based on the specific characteristics and requirements of the respective manufacturing system. Moreover, the framework is exemplified by three case studies from various industries and resulting potential are discussed. Full article
(This article belongs to the Special Issue Cyber Physical Production Systems)
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<p>Trade-off between error prevention and cost (adapted from [<a href="#B1-jmmp-04-00106" class="html-bibr">1</a>]).</p>
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<p>Exemplary cyber physical production system (CPPS) framework.</p>
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<p>Overview of the main components of a Quality Management System.</p>
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<p>Overview of Quality Gate Concept within the Manufacturing System (adapted from [<a href="#B25-jmmp-04-00106" class="html-bibr">25</a>]).</p>
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<p>Technical framework of virtual quality gates.</p>
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<p>Morphological box for the design of VQGs.</p>
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<p>Generalized battery cell production chain (adapted from [<a href="#B53-jmmp-04-00106" class="html-bibr">53</a>]).</p>
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<p>(<b>a</b>) Quality gate concept for Lithium-Ion Battery (LIB) cell production; (<b>b</b>) exemplarily depicted VQG in LIB Production (adapted from [<a href="#B45-jmmp-04-00106" class="html-bibr">45</a>]).</p>
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<p>VQG build through a hybrid data mining and visual analytics approach for casting of aluminum components: (<b>a</b>) graph-based visualization of class association rules plotted with the R-extension arulesViz; (<b>b</b>) interactive sensitivity analysis of features on the expected defects (NOK) ratio within Qlik Sense Desktop; (<b>c</b>) expected cumulative effect on NOK ratio reduction through several identified overlaying measures.</p>
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<p>Framework for data-based analysis of product state propagation through the eyes of visual analytics (adopted from [<a href="#B49-jmmp-04-00106" class="html-bibr">49</a>]).</p>
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<p>Resulting Sankey diagram exemplarily showing the propagation of product state classes from solder paste inspection (SPI) to automated optical inspection (AOI).</p>
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<p>Overview of different VQG specifications presented in case studies I–III.</p>
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11 pages, 4807 KiB  
Article
Micro-Structures Produced by Crystal Growth from Located Nuclei and Their Transfer Aiming at Functional Surfaces
by Nobuyuki Moronuki and Renato Serizawa
J. Manuf. Mater. Process. 2020, 4(4), 105; https://doi.org/10.3390/jmmp4040105 - 6 Nov 2020
Cited by 2 | Viewed by 2541
Abstract
Hydrothermal processes can produce regular micro-/nano-structures easily; but their placement or position is difficult to control, and the obtainable structures tend to be random. For controlling the crystal growth, two types of definite and regular structures were obtained. The first ones were ZnO [...] Read more.
Hydrothermal processes can produce regular micro-/nano-structures easily; but their placement or position is difficult to control, and the obtainable structures tend to be random. For controlling the crystal growth, two types of definite and regular structures were obtained. The first ones were ZnO urchin-like structures synthesized from located ZnO particles as the nuclei. These structures were found to work as gas sensors utilizing a wide surface area. The second one was a vertically aligned TiO2 nanorod array synthesized on a fluorine-doped tin oxide substrate that has a similar lattice constant to rutile TiO2. Super-hydrophobicity after ultraviolet irradiation was then examined. Finally, the synthesized TiO2 array was peeled off and transferred onto a resin sheet. We determined that the substrate could be subjected to repeated hydrothermal synthesis, thereby demonstrating the reusability of the substrate. These results demonstrate the applicability of these processes for industrial applications. Full article
(This article belongs to the Special Issue Progress in Precision Machining)
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<p>Schematics showing the aims of this study. (<b>a</b>) Hydrothermal synthesis is a simple process in a sealed container at an elevated temperature. Depending on the crystal structure and controlled nucleation, fine and regular structures can be obtained; (<b>b</b>) self-assembly of fine particles via the dip-coating process. Ideally, a monolayered packed structure will be obtained; (<b>c</b>) transfer of the synthesized structure with resin.</p>
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<p>Principle of the urchin-like profile production and arrangement of the nuclei. (<b>a</b>) Hexagonal close-packed structure of the ZnO crystal and its selective growth from a nucleus in multiple directions results in an urchin-like profile; (<b>b</b>) the arrangement of ZnO nuclei using the dip-coating process. The coverage increased with the number of dip-coating iterations [<a href="#B15-jmmp-04-00105" class="html-bibr">15</a>].</p>
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<p>Results of the urchin-like structure production showing the relationship between the reaction time and urchin diameter together with SEM pictures. The diameter increased linearly under these conditions [<a href="#B15-jmmp-04-00105" class="html-bibr">15</a>].</p>
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<p>Results of the performance test as a gas sensor: (<b>a</b>) Schematics showing the sensor structure with a picture. The electron exchange between the gas molecules and ZnO urchins changed the resistance of the structure. The urchin structure helps the electron exchange due to its wide surface area; (<b>b</b>) experimental results of ethanol gas sensing showing a comparison between the assembled particles and urchins. The low resistance and quick change provided excellent sensor performance [<a href="#B15-jmmp-04-00105" class="html-bibr">15</a>].</p>
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<p>Principle and experimental results for titanium dioxide (TiO<sub>2</sub>) nanorod synthesis: (<b>a</b>) Epitaxial crystal growth of TiO<sub>2</sub> on a fluorine-doped tin oxide (FTO) substrate requires similar lattice constants. The experimental results showed that the rod height increased linearly up to 6 μm, while further reactions caused peeling off from the rods; (<b>b</b>) results of SEM observation. Uniform aligned rod arrays were obtained when the reaction time was shorter than 4 h. Excess reaction time produced urchin-like structures on top.</p>
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<p>Characteristics of the synthesized TiO<sub>2</sub> rod array: (<b>a</b>) variations in the rod height of the good sample were less than 0.75 mm, while the bad sample presented variation of 15 μm; (<b>b</b>) a comparison of the x ray diffraction (XRD) results showing the crystallographically aligned structures of rutile TiO<sub>2</sub> [<a href="#B18-jmmp-04-00105" class="html-bibr">18</a>].</p>
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<p>Characteristics of the wettability of the synthesized TiO<sub>2</sub> surface: (<b>a</b>) UV irradiation changed the surface to superhydrophilic; (<b>b</b>) change in the water contact angle for one week after irradiation.</p>
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<p>Scheme for the transfer of self-assembled particles and the results: (<b>a</b>) Schematic of the particle transfer using half-cured resin; (<b>b</b>) SEM photos of the particle transfer results. Assembled particles are uniformly transferred upside-down on the resin layer, holding both monolayered and multi-layered particles [<a href="#B13-jmmp-04-00105" class="html-bibr">13</a>].</p>
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<p>Effect of imprint pressure on the embedded depth of the assembled SiO<sub>2</sub> particles. The depth of embedment can be changed with the imprint pressure between the substrates.</p>
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<p>Transfer of the TiO<sub>2</sub> rod array, its principle and its results: (<b>a</b>) The resin viscosity should be low to penetrate between the rods and have affinity with the rods to hold them during the transfer; (<b>b</b>) SEM photos of the results. The left two cases show that the resin reached the bottom of the rods, while the right image shows a case where the resin did not reach the bottom of the rods. Numbers in parentheses show the condition ID in <a href="#jmmp-04-00105-t004" class="html-table">Table 4</a>.</p>
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14 pages, 3761 KiB  
Article
CAD-Based Automated Design of FEA-Ready Cutting Tools
by Anastasios Tzotzis, César García-Hernández, José-Luis Huertas-Talón and Panagiotis Kyratsis
J. Manuf. Mater. Process. 2020, 4(4), 104; https://doi.org/10.3390/jmmp4040104 - 1 Nov 2020
Cited by 15 | Viewed by 4441
Abstract
The resources of modern Finite Element Analysis (FEA) software provide engineers with powerful mechanisms that can be used to investigate numerous machining processes with satisfying results. Nevertheless, the success of a simulation, especially in three dimensions, relies heavily on the accuracy of the [...] Read more.
The resources of modern Finite Element Analysis (FEA) software provide engineers with powerful mechanisms that can be used to investigate numerous machining processes with satisfying results. Nevertheless, the success of a simulation, especially in three dimensions, relies heavily on the accuracy of the cutting tool models that are implemented in the analyses. With this in mind, the present paper presents an application developed via Computer-Aided Design (CAD) programming that enables the automated design of accurate cutting tool models that can be used in 3D turning simulations. The presented application was developed with the aid of the programming resources of a commercially available CAD system. Moreover, the parametric design methodology was employed in order to design the tools according to the appropriate standards. Concluding, a sample tool model was tested by performing a number of machining simulations based on typical cutting parameters. The yielded results were then compared to experimental values of the generated machining force components for validation. The findings of the study prove the functionality of the tool models since a high level of agreement occurred between the acquired numerical results and the experimental ones. Full article
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<p>Basic geometric parameters of the SNGA120412S01525 (<b>a</b>), the CNGA120408T01020 (<b>b</b>) and the DNGA150404S01020 (<b>c</b>) inserts, along with their common sectioned view (<b>d</b>).</p>
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<p>The micro-geometry of a typical 80° diamond-shaped insert.</p>
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<p>The application’s interface and the corresponding code keys.</p>
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<p>The application’s workflow.</p>
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<p>The design workflow for the CNGA-family inserts: (<b>a</b>) the construction circle, (<b>b</b>) the contour, (<b>c</b>) the extrusion, (<b>d</b>) the corner radius, (<b>e</b>) the micro-geometry and (<b>f</b>) the clamping hole.</p>
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<p>The shape selector algorithm flowchart.</p>
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<p>The test framework including: (<b>a</b>) the Finite Element (FE) model setup, (<b>b</b>) the force diagrams and (<b>c</b>) the results.</p>
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<p>The model setup (<b>a</b>), the analysis domain (<b>b</b>) and the meshed tool (<b>c</b>).</p>
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<p>Simulated versus experimental machining force components: (<b>a</b>) the radial force, (<b>b</b>) the tangential force, (<b>c</b>) the feed force and (<b>d</b>) the resultant machining force.</p>
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15 pages, 3606 KiB  
Article
RFID Application in a Multi-Agent Cyber Physical Manufacturing System
by Maryam Farsi, Christina Latsou, John Ahmet Erkoyuncu and Geoffrey Morris
J. Manuf. Mater. Process. 2020, 4(4), 103; https://doi.org/10.3390/jmmp4040103 - 29 Oct 2020
Cited by 13 | Viewed by 3783
Abstract
In manufacturing supply chains with labour-intensive operations and processes, individuals perform various types of manual tasks and quality checks. These operations and processes embrace engagement with various forms of paperwork, regulation obligations and external agreements between multiple stakeholders. Such manual activities can increase [...] Read more.
In manufacturing supply chains with labour-intensive operations and processes, individuals perform various types of manual tasks and quality checks. These operations and processes embrace engagement with various forms of paperwork, regulation obligations and external agreements between multiple stakeholders. Such manual activities can increase human error and near misses, which may ultimately lead to a lack of productivity and performance. In this paper, a multi-agent cyber-physical system (CPS) architecture with radio frequency identification (RFID) technology is presented to assist inter-layer interactions between different manufacturing phases on the shop floor and external interactions with other stakeholders within a supply chain. A dynamic simulation model in the AnyLogic software is developed to implement the CPS-RFID solution by using the agent-based technique. A case study from cryogenic warehousing in cell and gene therapy has been chosen to test the validity of the presented CPS-RFID architecture. The analyses of the simulation results show improvement in efficiency and productivity, in terms of resource time-in-system. Full article
(This article belongs to the Special Issue Cyber Physical Production Systems)
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<p>PRISMA flow diagram and research methodology.</p>
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<p>Radio frequency identification (RFID) system architecture.</p>
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<p>Unified Modelling Language (UML) class diagram of multi-agent cyber physical manufacturing system.</p>
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<p>Cyber physical architecture of Internet of Things (IoT).</p>
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<p>UML composite structure diagram of a cryogenic supply chain.</p>
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<p>Case study: UML activity diagram for a cryogenic supply chain with RFID.</p>
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<p>Case study: UML use case of cell and gene therapy (CGT) cryogenic supply chain.</p>
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3 pages, 176 KiB  
Editorial
Advanced Manufacturing and Machining Processes
by Alborz Shokrani and Dirk Biermann
J. Manuf. Mater. Process. 2020, 4(4), 102; https://doi.org/10.3390/jmmp4040102 - 27 Oct 2020
Cited by 2 | Viewed by 2693
Abstract
Manufacturing is one of the major sections of the economy along with services, construction and agriculture [...] Full article
(This article belongs to the Special Issue Advanced Manufacturing and Machining Processes)
27 pages, 5875 KiB  
Review
On the Fabrication of Metallic Single Crystal Turbine Blades with a Commentary on Repair via Additive Manufacturing
by Nicole Marie Angel and Amrita Basak
J. Manuf. Mater. Process. 2020, 4(4), 101; https://doi.org/10.3390/jmmp4040101 - 26 Oct 2020
Cited by 28 | Viewed by 18595
Abstract
The turbine section of aircraft engines (both commercial and military) is an example of one of the most hostile environments as the components in this section typically operate at upwards of 1650 °C in the presence of corrosive and oxidative gases. The blades [...] Read more.
The turbine section of aircraft engines (both commercial and military) is an example of one of the most hostile environments as the components in this section typically operate at upwards of 1650 °C in the presence of corrosive and oxidative gases. The blades are at the heart of the turbine section as they extract energy from the hot gases to generate work. The turbine blades are typically fabricated using investment casting, and depending on the casting complexity, they generally display one of the three common microstructures (i.e., equiaxed or polycrystalline, directionally solidified, and single crystal). Single crystal casting is exotic as several steps of the casting process are traditionally hands-on. Due to the complex production process involving several prototyping iterations, the blade castings have a significant cost associated with them. For example, a set of 40 single crystal turbine blades costs above USD 600,000 and requires 60–90 weeks for production. Additionally, if the components suffer from material loss due to prolonged service or manufacturing defects, the traditional manufacturing methods cannot restore the parent metallurgy at the damage locations. Hence, there is a significant interest in developing additive manufacturing (AM) technologies that can repair the single crystal turbine blades. Despite the blades’ criticality in aircraft propulsion, there is currently no review article that summarizes the metallurgy, production process, failure mechanisms, and AM-based repair methods of the single crystal turbine blades. To address this existing gap, this review paper starts with a discussion on the composition of the single crystal superalloys, describes the traditional fabrication methods for the metallic single crystal turbine blades, estimates the material and energy loss when the blades are scrapped or reverted, and provides a summary of the AM technologies that are currently being investigated for their repair potential. In conclusion, based on the literature reviewed, this paper identifies new avenues for research and development approaches for advancing the fabrication and repair of single crystal turbine blades. Full article
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<p>A representative schematic showing the cooling mechanisms in a turbine blade (Reproduced from [<a href="#B3-jmmp-04-00101" class="html-bibr">3</a>] under the terms of the Creative Commons Attribution 3.0 License from <a href="http://creativecommons.org/licenses/by/3.0/" target="_blank">http://creativecommons.org/licenses/by/3.0/</a>).</p>
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<p>Representative images showing the (<b>a</b>) equiaxed, (<b>b</b>) directionally solidified, (<b>c</b>) single crystal microstructure. (<b>d</b>) Zoomed view of (<b>c</b>) illustrating the dendrite microstructure in single crystal turbine blades (Reproduced with permission from [<a href="#B5-jmmp-04-00101" class="html-bibr">5</a>], Copyright 2008 by The Minerals, Metals and Materials Society).</p>
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<p>(<b>a</b>) Turbine airfoil with worn-out blade tip, (<b>b</b>) cracking in the platform section, (<b>c</b>) tear in turbine blade (Reproduced from [<a href="#B9-jmmp-04-00101" class="html-bibr">9</a>] under the terms of the Creative Commons Attribution 4.0 License from <a href="http://creativecommons.org/licenses/by/4.0/" target="_blank">http://creativecommons.org/licenses/by/4.0/</a>), and (<b>d</b>) cracked turbine blades (Reproduced from [<a href="#B9-jmmp-04-00101" class="html-bibr">9</a>] under the terms of the Creative Commons Attribution 4.0 License from <a href="http://creativecommons.org/licenses/by/4.0/" target="_blank">http://creativecommons.org/licenses/by/4.0/</a>).</p>
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<p>(<b>a</b>) Microstructure of SX René N5 showing the formation of carbide precipitates. (<b>b</b>) A representative image showing the formation of γ/ γ′ microstructure in SX René N5.</p>
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<p>(<b>a</b>) Circular-clustered wax assembly (Reproduced from [<a href="#B21-jmmp-04-00101" class="html-bibr">21</a>] under the terms of the Creative Commons Attribution 4.0 License from <a href="http://creativecommons.org/licenses/by/4.0/" target="_blank">http://creativecommons.org/licenses/by/4.0/</a>); (<b>b</b>) schematic of a pigtail demonstrating how the turns in the block selector function to cull unwanted crystal orientations until only one orientation remains (Reproduced with permission from [<a href="#B24-jmmp-04-00101" class="html-bibr">24</a>]); (<b>c</b>) the shell mold corresponding to a wax assembly in (<b>a</b>) for casting SX blades (Reproduced from [<a href="#B21-jmmp-04-00101" class="html-bibr">21</a>] under the terms of the Creative Commons Attribution 4.0 License from <a href="http://creativecommons.org/licenses/by/4.0/" target="_blank">http://creativecommons.org/licenses/by/4.0/</a>); and (<b>d</b>) Cross-section of a ready-to-use mold demonstrating the pin placement used to stabilize the ceramic cores and the ceramic mold (Reproduced from [<a href="#B26-jmmp-04-00101" class="html-bibr">26</a>] under the terms of the Creative Commons Attribution 4.0 License from <a href="http://creativecommons.org/licenses/by/4.0/" target="_blank">http://creativecommons.org/licenses/by/4.0/</a>).</p>
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<p>(<b>a</b>) A representative vacuum Bridgman furnace showing the radiation baffle separating the heating and cooling zone. In this furnace, radiation heating affects the casting the most because it is the dominant form of heating (Adapted from [<a href="#B31-jmmp-04-00101" class="html-bibr">31</a>]). (<b>b</b>) Schematic of the liquid metal cooling-assisted casting (LMC) (Adapted from [<a href="#B21-jmmp-04-00101" class="html-bibr">21</a>]). (<b>c</b>) Schematic of the gas cooling casting (GCC) process (Adapted from [<a href="#B21-jmmp-04-00101" class="html-bibr">21</a>]).</p>
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<p>Schematic of the coating structure in the SX turbine blades (Adapted from [<a href="#B40-jmmp-04-00101" class="html-bibr">40</a>]).</p>
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<p>Scanning electron microscopy (SEM) images of microstructures after aging at 1000 °C for (<b>a</b>) 100 h, (<b>b</b>) 500 h, and (<b>c</b>) 1000 h. SEM images of microstructures aged at 1000 °C for (<b>d</b>,<b>g</b>) 100 h, (<b>e</b>,<b>h</b>) 500 h, and (<b>f</b>,<b>i</b>) 1000 h ruptured following creep deformation while subjected to 1140 °C/137 MPa: (<b>d</b>–<b>f</b>) the γ/γ′ microstructure and (<b>g</b>–<b>i</b>) representative interfacial dislocation networks. Figure (<b>a</b>) through (<b>i</b>) are reproduced with permission from [<a href="#B39-jmmp-04-00101" class="html-bibr">39</a>].</p>
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<p>(<b>a</b>) Material and energy required per year to produce SX blades, (<b>b</b>) material loss for three different scenarios, and (<b>c</b>) energy loss for three different scenarios.</p>
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<p>(<b>a</b>) Material and energy required per year to produce SX blades, (<b>b</b>) material loss for three different scenarios, and (<b>c</b>) energy loss for three different scenarios.</p>
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<p>Classification of AM processes. Green boxes represent the AM processes that have shown success in repairing simple geometry SX components to date.</p>
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<p>Representative optical images showing the capability of different AM processes in repairing a candidate SX alloy, CMSX-4<sup>®</sup>—(<b>a</b>) laser powder bed fusion (PBF) (L-PBF) (Reproduced with permission from [<a href="#B100-jmmp-04-00101" class="html-bibr">100</a>]), (<b>b</b>) E-PBF (Reproduced from [<a href="#B101-jmmp-04-00101" class="html-bibr">101</a>] under the terms of the Creative Commons Attribution 4.0 License from <a href="http://creativecommons.org/licenses/by/4.0/" target="_blank">http://creativecommons.org/licenses/by/4.0/</a>), and (<b>c</b>) laser-based DED (L-DED) (Reproduced with permission from [<a href="#B102-jmmp-04-00101" class="html-bibr">102</a>]). Electron backscatter diffraction (EBSD) refers to electron backscatter diffraction.</p>
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18 pages, 10724 KiB  
Article
Use of a Holistic Design and Manufacturing Approach to Implement Optimized Additively Manufactured Mould Inserts for the Production of Injection-Moulded Thermoplastics
by Loucas Papadakis, Stelios Avraam, Demetris Photiou, Simona Masurtschak and Juan Carlos Pereira Falcón
J. Manuf. Mater. Process. 2020, 4(4), 100; https://doi.org/10.3390/jmmp4040100 - 24 Oct 2020
Cited by 15 | Viewed by 4925
Abstract
Injection moulding is one the most familiar processes for manufacturing of plastic parts by injecting molten thermoplastic polymers into a metallic mould. The cycle time of this process consists of the phases of injection, packing, cooling, and ejection of the final product. Shortening [...] Read more.
Injection moulding is one the most familiar processes for manufacturing of plastic parts by injecting molten thermoplastic polymers into a metallic mould. The cycle time of this process consists of the phases of injection, packing, cooling, and ejection of the final product. Shortening of cycle time is a key consideration to increase productivity. Therefore, in this manuscript the adoption of additively manufactured mould inserts with conformal cooling channels by means of selective laser melting (SLM) with the aim to reduce process cycles is presented. The design and manufacture of a mould insert with conformal cooling channels for producing pressure fitting thermoplastic parts is described. Numerical analysis of the injection process and simulation of shape distortions after SLM were conducted providing useful results for the design and manufacture of the mould insert. The results of the numerical analyses are compared with experimental 3D geometrical data of the additively manufactured mould insert. Temperature measurements during the real injection moulding process demonstrating promising findings. The adoption of the introduced method for the series production of injection moulded thermoplastics proves a shortening of cycle times of up to 32% and a final product shape quality improvement of up to 77% when using mould inserts with conformal cooling channels over the conventional mould inserts. Full article
(This article belongs to the Special Issue Additive Manufacturing and Device Applications)
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<p>Different configurations of the mould insert cooling channels: (<b>a</b>) current mould insert geometry with conventional cooling channels; (<b>b</b>) Mould insert design variant with spiral conformal cooling channels; (<b>c</b>) mould insert design variant with crown conformal cooling channels.</p>
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<p>Process temperature reduction in injection moulded cap surface with utilization of crown conformal cooling channels calculated by means of transient thermo-mechanical finite element (FE) model with the aid of the software Moldex3D at 23 s, i.e., completion of injection phase with conformal cooling (left) compared to conventional cooling (right).</p>
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<p>Manufacturing process chain operations for the mould insert: (<b>a</b>) 3D printing by laser-based powder-bed fusion (L-PBF), (<b>b</b>) CNC machining of outer contour, (<b>c</b>) heat treatment, (<b>d</b>) electron discharged machining (EDM) of the mould insert cavity.</p>
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<p>CAD geometry evolution of the mould insert designed with the aid of the CAD software NX Siemens: (<b>a</b>) first design iteration; (<b>b</b>) final CAD geometry including necessary details for SLM process feasibility.</p>
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<p>L-PBF machine setting for the fabrication of the mould insert: (<b>a</b>) positioning, orientation and supports on the base plate; (<b>b</b>) support structure definition in the region of the horizontal shoulders with progressively increased diameter.</p>
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<p>Fabricated mould insert with conformal cooling channels after SLM process including support removal.</p>
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<p>Comparison of the shape accuracy to CAD ideal geometry of the: (<b>a</b>) 3D scanned mould insert fabricated by SLM; (<b>b</b>) simulated mould insert shape by means of FEA with the method of inherent strains after SLM and support removal.</p>
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<p>Tensile curves of maraging 300 (EN 1.2709) samples manufactured by SLM in LORTEK (as-built and direct aged with different temperatures for 6 h) [<a href="#B27-jmmp-04-00100" class="html-bibr">27</a>].</p>
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<p>Schematic cross-section view of the feeding process (top left), injection mould system including the stationary platen with mould inserts, polymer products and movable platen with mould threads (right) and injection moulding machine setup with alternate using of conformal and convectional mould inserts on a 6 series production mould as used by Elysee Irrigation Ltd.</p>
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<p>Fitting assembly for the connection of plastic pipes including all the involved components (left) and detailed technical drawing of the produced injection-moulded cap with tolerances according to DIN16742 TG5 (right).</p>
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<p>Average temperature measurements with infrared thermal camera immediately after ejection on mould cavity and on part for conformal and convectional cooling.</p>
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<p>Temperature measurements with infrared thermal camera after ejection demonstrating the temperature reduction in mould insert’s cavity when applying conformal cooling (top left) compared to conventional cooling (top right) and simulated temperatures with conformal cooling by means of FEA immediately after ejection with average temperature in the cavity of 36.6 °C (bottom).</p>
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<p>Temperature measurements with infrared thermal camera after ejection demonstrating the temperature reduction in mould insert’s cavity when applying conformal cooling (top left) compared to conventional cooling (top right) and simulated temperatures with conformal cooling by means of FEA immediately after ejection with average temperature in the cavity of 36.6 °C (bottom).</p>
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<p>Temperature measurements with infrared thermal camera after ejection demonstrating the temperature reduction on the cap product when applying conformal cooling (top left) compared to conventional cooling (top right) and simulated temperatures of cap with conformal cooling by means of FEA immediately after ejection with an average temperature of the cap of 110 °C (bottom).</p>
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<p>Temperature measurements with infrared thermal camera after ejection demonstrating the temperature reduction on the cap product when applying conformal cooling (top left) compared to conventional cooling (top right) and simulated temperatures of cap with conformal cooling by means of FEA immediately after ejection with an average temperature of the cap of 110 °C (bottom).</p>
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<p>Shape accuracy results of the fabricated injection-moulded cap measured with the aid of a RangeVision Spectrum 3D Scanning device compared to the target CAD geometry proving the high precision when using conformal cooling (left). Final FE-simulated shrunk cap shape after cooling down compared to the target CAD geometry (right) proving similar shape deviation on the outer cap skin.</p>
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<p>Unchanged ovality of inner cap threads with sinking cooling cycles when applying conformal cooling compared to overall lower dimensional accuracy and further worsening of the ovality of threads for shorter cycle time in the injection-moulding process with conventional cooling.</p>
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44 pages, 11315 KiB  
Review
The Capabilities of Spark-Assisted Chemical Engraving: A Review
by Zahraa Bassyouni and Jana D. Abou Ziki
J. Manuf. Mater. Process. 2020, 4(4), 99; https://doi.org/10.3390/jmmp4040099 - 23 Oct 2020
Cited by 6 | Viewed by 4432
Abstract
Brittle non-conductive materials, like glass and ceramics, are becoming ever more significant with the rising demand for fabricating micro-devices with special micro-features. Spark-Assisted Chemical Engraving (SACE), a novel micromachining technology, has offered good machining capabilities for glass and ceramic materials in basic machining [...] Read more.
Brittle non-conductive materials, like glass and ceramics, are becoming ever more significant with the rising demand for fabricating micro-devices with special micro-features. Spark-Assisted Chemical Engraving (SACE), a novel micromachining technology, has offered good machining capabilities for glass and ceramic materials in basic machining operations like drilling, milling, cutting, die sinking, and others. This paper presents a review about SACE technology. It highlights the process fundamentals of operation and the key machining parameters that control it which are mainly related to the electrolyte, tool-electrode, and machining voltage. It provides information about the gas film that forms around the tool during the process and the parameters that enhance its stability, which play a key role in enhancing the machining outcome. This work also presents the capabilities and limitations of SACE through comparing it with other existing micro-drilling and micromachining technologies. Information was collected regarding micro-channel machining capabilities for SACE and other techniques that fall under four major glass micromachining categories—mainly thermal, chemical, mechanical, and hybrid. Based on this, a figure that presents the capabilities of such technologies from the perspective of the machining speed (lateral) and resulting micro-channel geometry (aspect ratio) was plotted. For both drilling and micro-channel machining, SACE showed to be a promising technique compared to others as it requires relatively cheap set-up, results in high aspect ratio structures (above 10), and takes a relatively short machining time. This technique shows its suitability for rapid prototyping of glass micro-parts and devices. The paper also addresses the topic of surface functionalization, specifically the surface texturing done during SACE and other glass micromachining technologies. Through tuning machining parameters, like the electrolyte viscosity, tool–substrate gap, tool travel speed, and machining voltage, SACE shows a promising and unique potential in controlling the surface properties and surface texture while machining. Full article
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<p>Spark-Assisted Chemical Engraving (SACE) technology featuring the workpiece and metallic electrodes dipped in an electrolyte solution and connected through a DC voltage supply. Reprinted from the work in [<a href="#B6-jmmp-04-00099" class="html-bibr">6</a>] with permission from Elsevier.</p>
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<p>Schematics illustrating some of the machining operations that can be applied using SACE. (<b>a</b>) Drilling holes, (<b>b</b>) milling micro-channels and micro-grooves, (<b>c</b>) die sinking, (<b>d</b>) wire cutting, (<b>e</b>) turning, and (<b>f</b>) grinding.</p>
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<p>Schematics illustrating some of the machining operations that can be applied using SACE. (<b>a</b>) Drilling holes, (<b>b</b>) milling micro-channels and micro-grooves, (<b>c</b>) die sinking, (<b>d</b>) wire cutting, (<b>e</b>) turning, and (<b>f</b>) grinding.</p>
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<p>Schematic of a conventional SACE set-up. An XYZ Cartesian robot embodies a machining head (that holds the tool) and a processing cell containing the workpiece. Reprinted from the work in [<a href="#B30-jmmp-04-00099" class="html-bibr">30</a>] with permission from Elsevier.</p>
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<p>A schematic comparing the two most common types of machining.</p>
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<p>Difference in machining depth between (<b>a</b>) without using pulse voltage and vibrated electrolyte and (<b>b</b>) with pulse voltage and vibrated electrolyte. Republished with permission of Institute of Physics (IOP) Publishing, Ltd., from Geometric improvement of electrochemical discharge micro-drilling using an ultrasonic-vibrated electrolyte, Han et al., 19, 2009; permission conveyed through Copyright Clearance Center, Inc.</p>
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<p>The force signal and its corresponding current signal for a machining voltage of 33 V and feed rate of 15 µm/s. Reprinted from the work in [<a href="#B30-jmmp-04-00099" class="html-bibr">30</a>] with permission from Elsevier.</p>
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<p>(<b>a</b>) Reference position is taken when tool touches the surface (<b>b</b>) tool is pushed downwards with a certain distance (<b>c</b>) depth actuated with the Electrochemical discharge machining (ECDM) (<b>d</b>) tool stops as fixture goes back into equilibrium. Reprinted from the work in [<a href="#B31-jmmp-04-00099" class="html-bibr">31</a>] with permission from Elsevier.</p>
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<p>Drilling depth at 38 V with (<b>a</b>) gravity-feed method and (<b>b</b>) counter-resistant force method. Reprinted from the work in [<a href="#B31-jmmp-04-00099" class="html-bibr">31</a>] with permission from Elsevier.</p>
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<p>(<b>a</b>) The I–U characteristic curve during SACE. Reprinted from the work in [<a href="#B6-jmmp-04-00099" class="html-bibr">6</a>] with permission from Elsevier. (<b>b</b>) The gas film formation process around the tool-electrode.</p>
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<p>The different factors that affect the gas film.</p>
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<p>The gas film lifetime <math display="inline"><semantics> <mrow> <msub> <mi>T</mi> <mi>g</mi> </msub> </mrow> </semantics></math> and gas film formation time <math display="inline"><semantics> <mrow> <msub> <mi>T</mi> <mi mathvariant="normal">f</mi> </msub> </mrow> </semantics></math> as a function of applied voltage. Reprinted from the work in [<a href="#B55-jmmp-04-00099" class="html-bibr">55</a>] with permission from Elsevier.</p>
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<p>Current signals for different concentrations of KOH electrolyte at 40 V. Reprinted from the work in [<a href="#B62-jmmp-04-00099" class="html-bibr">62</a>] with permission from Elsevier.</p>
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<p>Distribution of spark energy for (<b>a</b>) Tapered tool and (<b>b</b>) Cylindrical tool [<a href="#B49-jmmp-04-00099" class="html-bibr">49</a>]. Reprinted from the work in [<a href="#B63-jmmp-04-00099" class="html-bibr">63</a>] with permission from Elsevier.</p>
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<p>The main effect plots of several parameters on the standard deviation of current. Reprinted from the work in [<a href="#B65-jmmp-04-00099" class="html-bibr">65</a>] with permission from Elsevier.</p>
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<p>Interaction plots showing stability of gas film (<b>a</b>) The interaction plot of electrolyte concentration and level of electrolyte (<b>b</b>) The interaction plot of the level of electrolyte and distance between the electrodes. Reprinted from the work in [<a href="#B65-jmmp-04-00099" class="html-bibr">65</a>] with permission from Elsevier.</p>
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<p>Surface wrinkles observed under Microscope on 0.4 M sample. Reprinted from the work in [<a href="#B72-jmmp-04-00099" class="html-bibr">72</a>] with permission from Elsevier.</p>
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<p>Variations in the average hole diameter for different tool electrode materials. Reprinted from the work in [<a href="#B86-jmmp-04-00099" class="html-bibr">86</a>] with permission from Elsevier.</p>
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<p>(<b>a</b>) The gas film surrounding the tool-electrode during SACE. (<b>b</b>) The thermal model of a tool-electrode performing SACE. <math display="inline"><semantics> <mrow> <msub> <mi>R</mi> <mrow> <mi>t</mi> <mi>o</mi> <mi>o</mi> <mi>l</mi> </mrow> </msub> </mrow> </semantics></math> and <math display="inline"><semantics> <mrow> <msub> <mi>R</mi> <mrow> <mi>l</mi> <mi>i</mi> <mi>q</mi> </mrow> </msub> </mrow> </semantics></math> are the heat transfer through the non-immersed part of the tool and the electrolyte, respectively, that connect the tool tip to the ambient temperature <math display="inline"><semantics> <mrow> <msub> <mi>T</mi> <mi>a</mi> </msub> </mrow> </semantics></math>. <span class="html-italic">C</span> is the heat capacitance, and <math display="inline"><semantics> <mrow> <msub> <mi>q</mi> <mi>i</mi> </msub> </mrow> </semantics></math> the heat generated by discharges. Reprinted from the work in [<a href="#B87-jmmp-04-00099" class="html-bibr">87</a>], International Journal of Advanced Manufacturing Technology, with permission from Springer.</p>
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<p>A schematic drawing of diamond-wire-sawing set-up [<a href="#B90-jmmp-04-00099" class="html-bibr">90</a>].</p>
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<p>Different tool-electrode geometries used in literature. (<b>a</b>) Tool with spherical end. (<b>b</b>) Micro-drill. (<b>c</b>) Electrode with a double-hole inner structure. (<b>d</b>) Array of stainless-steel tapered tools.</p>
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<p>Different parameter combinations for machining micro-holes using 30 wt% NaOH. Reprinted from the work in [<a href="#B94-jmmp-04-00099" class="html-bibr">94</a>] with permission from Elsevier.</p>
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<p>Micro-crack formation for 90% DR and smooth profile for 70% DR. Reprinted from the work in [<a href="#B96-jmmp-04-00099" class="html-bibr">96</a>] with permission from Elsevier.</p>
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<p>A 156 µm wide kerf machined at 40 V, 300 Hz, 60 DR, and 3000 rpm. Reprinted from the work in [<a href="#B97-jmmp-04-00099" class="html-bibr">97</a>] with permission from Elsevier.</p>
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<p>The Scanning Electron Microscope (SEM) of flattened end (<b>left</b>) and notched end (<b>right</b>). Reprinted from the work in [<a href="#B98-jmmp-04-00099" class="html-bibr">98</a>] with permission from Elsevier.</p>
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<p>Variation of Overcut (<b>a</b>) and HAZ (<b>b</b>) as a function of Voltage and Tool feed rate. Reprinted from the work in [<a href="#B99-jmmp-04-00099" class="html-bibr">99</a>] with permission from Elsevier.</p>
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<p>Variations of Entrance diameter and machining time as a function of the pulse off time. Republished with permission of IOP publishing, Ltd., from “The tool geometrical shape and pulse-off time of pulse voltage effects in a Pyrex glass electrochemical discharge microdrilling process”, Zheng et al., 17, 2007; permission conveyed through Copyright Clearance Center, Inc.</p>
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<p>Effect of some process parameters (detailed in <a href="#jmmp-04-00099-t003" class="html-table">Table 3</a>) on surface roughness (<b>a</b>) and entrance diameter/width (<b>b</b>). Note that the letters on the x-axis refer to the type of process improvement, detailed in <a href="#jmmp-04-00099-t003" class="html-table">Table 3</a>.</p>
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<p>Feed rate (<b>a</b>) and surface roughness (<b>b</b>) vs. aspect ratio for four categories of glass drilling operations [<a href="#B119-jmmp-04-00099" class="html-bibr">119</a>].</p>
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<p>The variations of speed rate (µm/s) vs. aspect ratio of the machined micro-channel for different micromachining technologies, clustered into zones depending on the machining type. The machining techniques belong to four major categories (chemical, thermal, mechanical, and hybrid methods), each represented by a different color. Note that the aspect ratio refers to the depth per machining pass divided by the width of the micro-channel and the speed refers to horizontal speed along the micro-channel length.</p>
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<p>Surface texture of glass micro-channels for different electrolyte concentrations (Process parameters: 28 V applied voltage, 5 µm/s tool speed; Electrolyte: NaOH; Tool: 500 µm stainless-steel). Reprinted from the work in [<a href="#B14-jmmp-04-00099" class="html-bibr">14</a>] with permission from Elsevier.</p>
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<p>SEM screenshots of line, circle, and square patterns. Reprinted from the work in [<a href="#B128-jmmp-04-00099" class="html-bibr">128</a>] with permission from Elsevier.</p>
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<p>Surfaces with different micro-textures and profiles, depending on the powder type and sintering conditions. Reprinted from the work in [<a href="#B132-jmmp-04-00099" class="html-bibr">132</a>] with permission from Elsevier.</p>
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<p>SEM micrographs showing the different formed patterns at (<b>a</b>) multiple pits (holes), (<b>b</b>) individual pits, and (<b>c</b>) bottom of pits. Reprinted from the work in [<a href="#B140-jmmp-04-00099" class="html-bibr">140</a>] with permission from Elsevier.</p>
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<p>Atomic Force Microscopy (AFM) images of a glass substrate after polishing [<a href="#B141-jmmp-04-00099" class="html-bibr">141</a>].</p>
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<p>AFM images of sol–gel-coated substrates mechanically textured [<a href="#B142-jmmp-04-00099" class="html-bibr">142</a>].</p>
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16 pages, 5438 KiB  
Article
A Study on Strengthening Mechanical Properties of a Punch Mold for Cutting by Using an HWS Powder Material and a DED Semi-AM Method of Metal 3D Printing
by Seong-Woong Choi, Yong-Seok Kim, Young-Jin Yum and Soon-Yong Yang
J. Manuf. Mater. Process. 2020, 4(4), 98; https://doi.org/10.3390/jmmp4040098 - 27 Sep 2020
Cited by 4 | Viewed by 4336
Abstract
The post-processing (punching or trimming) of high-strength parts reinforced by hot stamping requires punch molds with improved mechanical properties in hardness, resistance to wear, and toughness. In this study, a semi-additive manufacturing (semi-AM) method of heterogeneous materials was proposed to strengthen these properties [...] Read more.
The post-processing (punching or trimming) of high-strength parts reinforced by hot stamping requires punch molds with improved mechanical properties in hardness, resistance to wear, and toughness. In this study, a semi-additive manufacturing (semi-AM) method of heterogeneous materials was proposed to strengthen these properties using high wear resistance steel (HWS) powder and directed energy deposition (DED) technology. To verify these mechanical properties as a material for the punch mold for cutting, specimens were prepared and tested by a semi-AM method of heterogeneous material. The test results of the HWS additive material by the semi-AM method proposed in this study are as follows: the hardness was 60.59–62.0 HRc, which was like the Bulk D2 specimen. The wear resistance was about 4.2 times compared to that of the D2 specimen; the toughness was about 4.0 times that of the bulk D2 specimen; the compressive strength was about 1.45 times that of the bulk D2 specimen; the true density showed 100% with no porosity. Moreover, the absorption energy was 59.0 J in a multi-semi-AM specimen of heterogeneous materials having an intermediate buffer layer (P21 powder material). The semi-AM method of heterogeneous materials presented in this study could be applied as a method to strengthen the punch mold for cutting. In addition, the multi-semi-AM method of heterogeneous materials will be able to control the mechanical properties of the additive material. Full article
(This article belongs to the Special Issue Additive Manufacturing and Device Applications)
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<p>Device configuration and additive layer concept in directed energy deposit (DED) systems.</p>
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<p>SEM images of samples before and after sieving of the high wear resistance steel (HWS) powder: (<b>a</b>) Powder states before sieving; (<b>b</b>) Powder states after sieving; (<b>c</b>,<b>d</b>) Particle shape of satellite powder.</p>
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<p>Specimen concept design for the evaluation of the properties of additive manufacturing (AM) material: (<b>a</b>) Design shape of the AM specimen for the compressive strength test and density measurement; (<b>b</b>) Design shape of the AM specimen for the impact absorption energy measurement; (<b>c</b>) Design shape of the AM specimens for the wear resistance and hardness tests.</p>
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<p>Foundation specimens and machined specimen with semi-AM heterogeneous materials: (<b>a</b>) Basic specimen before machining for the compression test and the finished specimen after machining; (<b>b</b>) Basic specimen for the impact test specimens and the finished specimen after machining; (<b>c</b>) Basic specimen before machining and the finished wear specimen after machining.</p>
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<p>State of the specimen after the hardness test: (<b>a</b>) HWS AM material part of the wear specimen; (<b>b</b>) D2 substrate material part of the wear specimen.</p>
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<p>The hardness comparison of the three materials.</p>
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<p>State of the specimen after wear testing: (<b>a</b>) State of the specimen before the abrasion test; (<b>b</b>) State of wear traces upon which a wear track occurred on the surface of the specimen due to the mechanical action between the ball surface and the specimen; (<b>c</b>) SEM images of the wear track before heat treatment of the HWS AM specimen; (<b>d</b>) SEM images of the wear track after heat treatment of the HWS AM specimen.</p>
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<p>The wear-resistant comparison of the three materials.</p>
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<p>State of the specimens after impact testing for full-AM HWS and HWS- P21 AM specimens: (<b>a</b>) Full-AM specimen; (<b>b</b>) HWS-P21 semi-AM specimen.</p>
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<p>The impact absorber energy comparison of the five materials.</p>
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<p>The compressive strength comparison of the three materials.</p>
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<p>The specimen image after the density measurement test: (<b>a</b>) Void state images before heat treating the AM specimen of the HWS powder material; (<b>b</b>) Void state images after heat treating the AM specimen of the HWS powder material.</p>
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<p>The true density comparison of the three materials.</p>
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24 pages, 8440 KiB  
Article
Data-Driven Digital Twins for Technical Building Services Operation in Factories: A Cooling Tower Case Study
by Christine Blume, Stefan Blume, Sebastian Thiede and Christoph Herrmann
J. Manuf. Mater. Process. 2020, 4(4), 97; https://doi.org/10.3390/jmmp4040097 - 23 Sep 2020
Cited by 31 | Viewed by 6141
Abstract
Cyber-physical production systems (CPPS) and digital twins (DT) with a data-driven core enable retrospective analyses of acquired data to achieve a pervasive system understanding and can further support prospective operational management in production systems. Cost pressure and environmental compliances sensitize facility operators for [...] Read more.
Cyber-physical production systems (CPPS) and digital twins (DT) with a data-driven core enable retrospective analyses of acquired data to achieve a pervasive system understanding and can further support prospective operational management in production systems. Cost pressure and environmental compliances sensitize facility operators for energy and resource efficiency within the whole life cycle while achieving reliability requirements. In manufacturing systems, technical building services (TBS) such as cooling towers (CT) are drivers of resource demands while they fulfil a vital mission to keep the production running. Data-driven approaches, such as data mining (DM), help to support operators in their daily business. Within this paper the development of a data-driven DT for TBS operation is presented and applied on an industrial CT case study located in Germany. It aims to improve system understanding and performance prediction as essentials for a successful operational management. The approach comprises seven consecutive steps in a broadly applicable workflow based on the CRISP-DM paradigm. Step by step, the workflow is explained including a tailored data pre-processing, transformation and aggregation as well as feature selection procedure. The graphical presentation of interim results in portfolio diagrams, heat maps and Sankey diagrams amongst others to enhance the intuitive understanding of the procedure. The comparative evaluation of selected DM algorithms confirms a high prediction accuracy for cooling capacity (R2 = 0.96) by using polynomial regression and electric power demand (R2 = 0.99) by linear regression. The results are evaluated graphically and the transfer into industrial practice is discussed conclusively. Full article
(This article belongs to the Special Issue Cyber Physical Production Systems)
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<p>Components and parameters of an industrial cooling tower system based on [<a href="#B25-jmmp-04-00097" class="html-bibr">25</a>].</p>
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<p>Data-driven approaches and proposed workflow to create a digital twin.</p>
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<p>Workflow to create a data-driven digital twin.</p>
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<p>Data mining algorithms selected for the case study.</p>
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<p>Scheme of considered industrial cooling tower system with relevant measurands.</p>
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<p>Heatmap of weekly electric power demand for one year, classified by weekdays.</p>
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<p>(<b>a</b>) Boxplot of energy efficiency ratio (EER) for cooling tower (CT) system over the year (based on daily data); (<b>b</b>) EER in relation to ambient temperature (based on hourly data, coloring indicates related operation month).</p>
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<p>(<b>a</b>) Portfolio analysis to characterize energy efficiency ratio (EER) of CT inspired by the energy portfolio in [<a href="#B16-jmmp-04-00097" class="html-bibr">16</a>]; (<b>b</b>) application of portfolio analysis (hourly data, coloring indicates related operation month).</p>
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<p>Box plots of cooling capacity and electric power demand: (<b>a</b>) before outlier filtering; (<b>b</b>) after outlier filtering.</p>
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<p>Correlation matrix indicates data interdependencies with positive linear correlation (<b>green color</b>) and negative linear correlation (<b>red color</b>).</p>
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<p>Sankey diagram of data quantity development through data aggregation and data transformation, unit is total number of data.</p>
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<p>Mean squared errors (MSE) from feature selection for linear regression (LR), simple regression tree (SRT) and multilayer perception (MLP) predicting the electric power demand.</p>
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<p>Heatmap from feature selection indicating relevance of variables for selected algorithms assessed for electric power demand (dark grey color indicates high relevance).</p>
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<p>Surface plot of hyperparameter assessment: (<b>a</b>) R<sup>2</sup> for simple regression tree algorithm; (<b>b</b>) R<sup>2</sup> for multilayer perception algorithm.</p>
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<p>Evaluation of data mining results predicting the cooling capacity.</p>
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<p>Time series plot of original and predicted cooling capacity and resulting error predicted with polynomial regression (PR) algorithm.</p>
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<p>Evaluation of data mining results predicting the electric power.</p>
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<p>Time series plot of original and predicted electric power demand and resulting error predicted with linear regression (LR) algorithm.</p>
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<p>Summary of data mining results predicting the cooling capacity.</p>
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<p>Summary of data mining results predicting the electric power demand.</p>
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