Material Allowable Generation and AM Process Parameters E ﬀ ect on Porosity

: Additive manufacturing (AM) process methods such as powder bed fusion (LPBF) of metal powder layers can produce layered material systems with designed microstructures, which may exhibit scatter in mechanical properties (e.g., lower yield and lower failure strain), corrosion due to porosity and print anomalies. This study shows the development of AM process simulation to predict As-built material characteristic and their scatter comparing with experimental test data. ICME (Integrated Computational Materials Engineering) was used to simulate yield, ultimate, strain, and reduction of the area of sample AM. The method was extended to predict oxidation and damage of as-built parts. The samples were fabricated horizontally and vertically in multiple and scatter directions to ﬁnd the e ﬀ ect on the mechanical properties such as ultimate tensile strength (UTS) and yield strength (YS). The probabilistic sensitivities show that in order for the next-generation technology to improve the strength of 3D printed materials, they must control the void volume fraction (trapped gas) and orientation of voids. The studied 3D print modality processes: (a) LPBF of AlSi10Mg, and (b) Electron Beam (EBM) of Ti-6Al-4V materials are shown to be over 99.99% reliable. The statistics of 3D printed Ti-6Al-4V have been observed for room and high temperature (RT / HT). The ICME Material Characterization and Qualiﬁcation (MCQ) software material model prediction capabilities were used to predict (a) Material Allowable, a variation in Stress Strain Curves Characteristic Points and Residual Stress due to air particle (void / defect) shape and size and orientation. The probabilistic simulation computes Cumulative Distribution Function (CDF) and probabilistic sensitivities for YS, UTS, and %Elongation as well as A and B basis allowable of the As-Built 3D printed material and; and (b) Fracture Control Plan fracture toughness determination, and fatigue crack growth vs. stress intensity. of Thermal History in

Material Jetting. Each modality has its own quirks and shortcomings when attempting to fabricate qualified parts while avoiding build anomalies. Identifying the correct process parameters to achieve this goal generally involves trial and error. Further, print strategy can vary from machine to machine. As such, manufacturing

AM Part Qualification
AM LPBF material exhibits scatter and uncertainty due to various build anomalies (Table 1) and variation in machine parameters (Table 2). It should be noted that the referenced anomalies correspond to manufacturing errors that must be measured, controlled and mitigated in order to achieve part qualification as dictated by NIST, DOD, and ASTM [1 -3]. Since each process parameter may impact the results of a build, it is critical to assess the sensitivity of each parameter in relation to the referenced anomalies.

AM Part Qualification
AM LPBF material exhibits scatter and uncertainty due to various build anomalies (Table 1) and variation in machine parameters (Table 2). It should be noted that the referenced anomalies correspond to manufacturing errors that must be measured, controlled and mitigated in order to achieve part qualification as dictated by NIST, DOD, and ASTM [1 -3]. Since each process parameter may impact the results of a build, it is critical to assess the sensitivity of each parameter in relation to the referenced anomalies. For example, variation in one parameter, such as hatch spacing, can result in dramatic changes to stable and unstable print zones in an AM LPBF process. The key steps in the qualification of AM parts are: (1) optimization of process parameters; (2) porosity minimization; (3) surface roughness minimization; (4) tolerance minimization and net shape assessment due to residual stresses, baseplate removal, and residual deflection; (5) prediction of mechanical properties and stress-strain curve, as well as scatter and uncertainty of yield and ultimate stress/and strain; (6) establishment of fracture control plan and accepted threshold crack size; (7) effect of post heat treatment on part quality; and (8) part performance under service loading. Primary (Controllable) Process Parameters, shown in Table 2, are a subset of all 55 parameters [4] non controllable (not allowed by machine) and approximately 10 (EBAM®). Data necessary to support part qualification may be taken from either: (1) in situ AM machine sensory data (i.e., photo diode, thermal camera, profilometer, meltpool, surface roughness, temperature heat flux) and/or; (2) ICME-generated tool sets such as: (a) thermal management tools for prediction of: (i) melt pool, (ii) process map, and (iii) micro void generation; and (b) material modeling, characterization, and qualification tools for predicting the stress-strain curve, residual stress/strain, and mechanical property such as strength, allowables, uncertainty/sensitivity generation and fracture property control prediction.

Machine Process and Modality (LPBF, EBM)
Powder Bed Fusion (PBF) is one of the seven categories of AM processes defined in ASTM F2792 [5]. PBF processes use thermal energy to selectively fuse areas of a layer of powder using laser or an electron beam as the energy source [6]. When the energy source traces the geometry of an individual layer onto the top surface of the powder bed, the energy from the beam spot is absorbed by the exposed powder, causing that powder to melt. This small molten area is often described as the melt-pool. Individual powder particles are fused together when the melt-pool re-solidifies. After one layer is completed, the build platform is lowered by the prescribed layer thickness, and a new layer of Coatings 2020, 10, 625 4 of 22 powder from the dispenser platform is swept over the build platform, filling the resulting gap and allowing a new layer to be built.
Some varieties/variations of Powder Bed Fusion (PBF) processes use low-power lasers to bind powder particles by only melting the surface of the powder particles (called selective laser sintering or SLS) or a binder coating the powder particles. These processes produce green parts that require further post-processing to infiltrate and sinter the parts to make them fully dense. Another class of PBF processes uses high-power energy beams to fully melt the powder particles, which then fuse together to the previous layer(s) when the molten material cools, e.g., selective laser melting (SLM), direct metal laser sintering (DMLS), or electron-beam melting (EBM). Repeating this process, layer-by-layer, directly results in a part with near 100% density, even in metals. These processes are of primary interest to this study.
The electron Beam Melting (EBM) machine process includes: (1) CAD File Sliced into thin layers, (2) coils used for focus and scanning and (3) electrons accelerated onto a powder bed. Advantages include: (a) No tooling required-unlike castings; (b) performed in vacuum environment-produces clean material; (c) performed in a hot powder bed-allows for complex shapes, stress relief as part of process, and no residual stresses; (d) melting takes places in seconds-extremely fine grain size; (e) process is rapid-10 lb part fabricated within 24 h; and (f) powder utilization is nearly >90%.
Disadvantages include: (1) produces a coarse surface finish; (2) design must allow for powder removal; (3) maximum size of machine build volume: 8" × 8" × 14"; and (4) exhibits oxidation on some powder materials. Figure 2 shows the Electron Beam Melted vs. Wrought for Ti-6Al-4V Microstructure Comparison. As shown, the material Characteristics are: (i) Uniform, Fine Grain; (ii) Columnar; (iii) Lamellar Alpha Phase; and (iv) Larger Beta Grain. The source of unconsolidated powder as shown in Figure 2 is not understood. This type of flaw is similar to a leaner defect and will drastically impacts the fatigue life of the EBM parts.
Coatings 2020, 10, 625 4 of 23 PBF processes uses high-power energy beams to fully melt the powder particles, which then fuse together to the previous layer(s) when the molten material cools, e.g., selective laser melting (SLM), direct metal laser sintering (DMLS), or electron-beam melting (EBM). Repeating this process, layerby-layer, directly results in a part with near 100% density, even in metals. These processes are of primary interest to this study. The electron Beam Melting (EBM) machine process includes: (1) CAD File Sliced into thin layers, (2) coils used for focus and scanning and (3) electrons accelerated onto a powder bed. Advantages include: (a) No tooling required-unlike castings; (b) performed in vacuum environment-produces clean material; (c) performed in a hot powder bed-allows for complex shapes, stress relief as part of process, and no residual stresses; (d) melting takes places in seconds-extremely fine grain size; (e) process is rapid-10 lb part fabricated within 24 h; and (f) powder utilization is nearly >90%.
Disadvantages include: (1) produces a coarse surface finish; (2) design must allow for powder removal; (3) maximum size of machine build volume: 8" × 8" × 14"; and (4) exhibits oxidation on some powder materials. Figure 2 shows the Electron Beam Melted vs. Wrought for Ti-6Al-4V Microstructure Comparison. As shown, the material Characteristics are: (i) Uniform, Fine Grain; (ii) Columnar; (iii) Lamellar Alpha Phase; and (iv) Larger Beta Grain. The source of unconsolidated powder as shown in Figure 2 is not understood. This type of flaw is similar to a leaner defect and will drastically impacts the fatigue life of the EBM parts.
The microstructure produced using electron beam powder bed (EBPB) and laser beam powder bed (LBPB) techniques as well as wire fed laser beam (WFLB) is a typical alpha/beta microstructure of Ti-6Al-4V. The morphology of the porosity for EBPB and LBPB differed significantly [7]. The LBPBprocessed material exhibited irregular-shaped pores, whereas the EBPB produced spherical pores. It may be further noted that the DMLS systems produced surfaces approximately twice as smooth as the EBM. The surface condition is most important for fatigue critical parts intended for use in their "as-fabricated" net shape condition. This is especially relevant for parts with complex internal features where surface finishing of entire part may be impracticable.  The microstructure produced using electron beam powder bed (EBPB) and laser beam powder bed (LBPB) techniques as well as wire fed laser beam (WFLB) is a typical alpha/beta microstructure of Ti-6Al-4V. The morphology of the porosity for EBPB and LBPB differed significantly [7]. The LBPB-processed material exhibited irregular-shaped pores, whereas the EBPB produced spherical pores. It may be further noted that the DMLS systems produced surfaces approximately twice as smooth as the EBM. The surface condition is most important for fatigue critical parts intended for use in their "as-fabricated" net shape condition. This is especially relevant for parts with complex internal features where surface finishing of entire part may be impracticable.
In summary, when properly processed, the static mechanical properties of AM metallic materials are comparable to conventionally fabricated metallic components. The relatively high cooling rates achieved reduce partitioning and favor reduced grain sizes. However, AM-fabricated materials do exhibit microstructural and mechanical property anisotropy with the Z-direction generally being the weakest. Dynamic properties of AM produced alloys are dominated by defect structures, viz., micro-porosity and surface finish. However, properly processed HIPed and finished machined AM alloys can exhibit fatigue properties on parity with those of wrought alloys.

Allowable Generation
The direct computation methods of the MMPDS [2] are appropriate to determine the T99 values for this design value assessment for ultimate tensile strength (UTS). Evaluation of the Pearson (three-parameter gamma) and Weibull distributions using the appropriate modified Anderson-Darling tests show that either distribution is acceptable. The Pearson model gives a T99 for the UTS of 191.0 for 17-4 PH stainless steel, which is seen as a high value [2]. The data and fit are illustrated in Figure 3. Tensile testing for UTS, yield strength (YS), and elongation according to ASTM E8/E8M, Standard Test Methods for Tension Testing of Metallic Materials, is required for all builds. For consistency in evaluation, tensile witness specimen geometry and build orientation are standardized to remain consistent with those specimens used to establish the acceptance criteria. Tensile witness specimens are expected to represent the full Z-height of the build and, to the degree possible, be positioned behind the part relative to the travel direction of the powder re-coater. Tensile specimens are commonly stacked atop each other to cover the Z-height of the build. Depending on the part height and tensile specimen design, more than one stack is generally needed. The best policy is to allow for alternating tensile specimen gage locations in the stacks to provide the best possible test coverage of the Z-height [3]. In summary, when properly processed, the static mechanical properties of AM metallic materials are comparable to conventionally fabricated metallic components. The relatively high cooling rates achieved reduce partitioning and favor reduced grain sizes. However, AM-fabricated materials do exhibit microstructural and mechanical property anisotropy with the Z-direction generally being the weakest. Dynamic properties of AM produced alloys are dominated by defect structures, viz., microporosity and surface finish. However, properly processed HIPed and finished machined AM alloys can exhibit fatigue properties on parity with those of wrought alloys.

Allowable Generation
The direct computation methods of the MMPDS [2] are appropriate to determine the T99 values for this design value assessment for ultimate tensile strength (UTS). Evaluation of the Pearson (threeparameter gamma) and Weibull distributions using the appropriate modified Anderson-Darling tests show that either distribution is acceptable. The Pearson model gives a T99 for the UTS of 191.0 for 17-4 PH stainless steel, which is seen as a high value [2]. The data and fit are illustrated in Figure  3. Tensile testing for UTS, yield strength (YS), and elongation according to ASTM E8/E8M, Standard Test Methods for Tension Testing of Metallic Materials, is required for all builds. For consistency in evaluation, tensile witness specimen geometry and build orientation are standardized to remain consistent with those specimens used to establish the acceptance criteria. Tensile witness specimens are expected to represent the full Z-height of the build and, to the degree possible, be positioned behind the part relative to the travel direction of the powder re-coater. Tensile specimens are commonly stacked atop each other to cover the Z-height of the build. Depending on the part height and tensile specimen design, more than one stack is generally needed. The best policy is to allow for alternating tensile specimen gage locations in the stacks to provide the best possible test coverage of the Z-height [3]. Print orientation effect on tensile strength and strain has an effect on Tensile properties of the vertically and horizontally oriented SLM 17-4 PH SS specimens, in either their as-built (AB) or heat treated (HT) condition [8] are presented in Figure 4. The results indicate that building orientation during SLM and post-manufacturing heat treatment (solution annealing plus peak-aging) have significant effects on the monotonic tensile behavior of SLM 17-4 PH SS. Yield and ultimate tensile strengths were significantly affected by the post-manufacturing heat treatment, while elongation to failure was mostly influenced by part building orientation. The effects of heat treatment on the investigated SLM parts are attributed to the formation of precipitates in the material matrix, as well as the altering of other microstructural features, i.e., phase volume fraction, grain size and morphology, while the build orientation has direct influence on the damage evolution under loading. Print orientation effect on tensile strength and strain has an effect on Tensile properties of the vertically and horizontally oriented SLM 17-4 PH SS specimens, in either their as-built (AB) or heat treated (HT) condition [8] are presented in Figure 4. The results indicate that building orientation during SLM and post-manufacturing heat treatment (solution annealing plus peak-aging) have significant effects on the monotonic tensile behavior of SLM 17-4 PH SS. Yield and ultimate tensile strengths were significantly affected by the post-manufacturing heat treatment, while elongation to failure was mostly influenced by part building orientation. The effects of heat treatment on the investigated SLM parts are attributed to the formation of precipitates in the material matrix, as well as the altering of other microstructural features, i.e., phase volume fraction, grain size and morphology, while the build orientation has direct influence on the damage evolution under loading. A part's building orientation during SLM influences its cooling rate (due to the part's aspect ratio), and thus encumbered microstructure, while the final orientation of deposited layers (which depend on build direction) impacts part strength in various loading directions. For instance, the vertically oriented SLM samples consist of deposited layers perpendicular to the investigated loading direction and this can impact its tensile strength [8].
Coatings 2020, 10, 625 6 of 23 A part's building orientation during SLM influences its cooling rate (due to the part's aspect ratio), and thus encumbered microstructure, while the final orientation of deposited layers (which depend on build direction) impacts part strength in various loading directions. For instance, the vertically oriented SLM samples consist of deposited layers perpendicular to the investigated loading direction and this can impact its tensile strength [8].

Methodology
The defined approach is based on ICME-driven Thermal Modeling and Material Characterization-Qualification (MCQ) including Fracture toughness determination, and fatigue crack growth Model. In the following paragraphs, each critical module will be explained in detail.

ICME Simulation Elements
The individual components of ICME simulation consist of Multi-Scale Modeling of Thermal, Mechanical, Material properties, Process Modeling, and Part Qualification with/without In-Situ Monitoring [9]. They in turn support: (1) A thermal management approach to rapidly calculate thermal profile, material state and process map, (2) a global local FEM approach to calculate cracks, oxidation, surface roughness using diffusional creep approach, (3) a fracture mechanics approach to determine fracture properties for a 3D printed material system and (4) a DOE (design of Experiment ) Surrogate Meta modeling approach is used to optimize print parameters to minimize surface roughness and obtain a better surface finish. ASC's current ICME-based 3D printing capability will be used as baseline for the proposed metal AM process simulation. The current 3D printing computational tools include material characterization, machine G-code data processing, mesh generation from G-code, STL file smoothing, as well as assessment of distortion, residual stress, deflection and damage and fracture evolution using a coupled thermo-mechanical solution for both metal and polymer-reinforced plastics. Figure 5 depicts the current process flow strategy including material modeling and part qualification. Material Characterization and Qualification (MCQ) software capability accounts for inclusion (particulate) to formulate the stress-strain curve in both the longitudinal and transverse direction. Micromechanics and fracture mechanics approaches have been developed (Figure 5a) for the evaluation of the overall properties of heterogeneous materials and their dependence on the properties of constituents and the microstructure of materials. They are mainly based on Eshelby's equivalent inclusion theory [10]. A nano-micromechanics-based theory proposed by Mori-Tanaka and Eshelby is used to demonstrate the capability of MCQ software to predict stress-strain curves with effect of inclusions.

Methodology
The defined approach is based on ICME-driven Thermal Modeling and Material Characterization-Qualification (MCQ) including Fracture toughness determination, and fatigue crack growth Model. In the following paragraphs, each critical module will be explained in detail.

ICME Simulation Elements
The individual components of ICME simulation consist of Multi-Scale Modeling of Thermal, Mechanical, Material properties, Process Modeling, and Part Qualification with/without In-Situ Monitoring [9]. They in turn support: (1) A thermal management approach to rapidly calculate thermal profile, material state and process map, (2) a global local FEM approach to calculate cracks, oxidation, surface roughness using diffusional creep approach, (3) a fracture mechanics approach to determine fracture properties for a 3D printed material system and (4) a DOE (design of Experiment ) Surrogate Meta modeling approach is used to optimize print parameters to minimize surface roughness and obtain a better surface finish. ASC's current ICME-based 3D printing capability will be used as baseline for the proposed metal AM process simulation. The current 3D printing computational tools include material characterization, machine G-code data processing, mesh generation from G-code, STL file smoothing, as well as assessment of distortion, residual stress, deflection and damage and fracture evolution using a coupled thermo-mechanical solution for both metal and polymer-reinforced plastics. Figure 5 depicts the current process flow strategy including material modeling and part qualification. Material Characterization and Qualification (MCQ) software capability accounts for inclusion (particulate) to formulate the stress-strain curve in both the longitudinal and transverse direction. Micromechanics and fracture mechanics approaches have been developed (Figure 5a) for the evaluation of the overall properties of heterogeneous materials and their dependence on the properties of constituents and the microstructure of materials. They are mainly based on Eshelby's equivalent inclusion theory [10]. A nano-micromechanics-based theory proposed by Mori-Tanaka and Eshelby is used to demonstrate the capability of MCQ software to predict stress-strain curves with effect of inclusions. For Fracture Toughness Determination (FTD), the extended the Griffith theory is used to estimate the fracture toughness value of metallic alloys from simple uniaxial tensile tests. For Fatigue Crack Growth (FCG), the Fatigue Crack Growth rate curve (or da/dN vs. ΔK) can be generated by applying the fracture toughness value, KC (obtained from the extended Griffith theory) for the accelerated region, Paris region, and threshold regions [11].
Part qualification uses Durability and Damage Tolerance (D and DT) to assess the integrity of complex structures by performing a Multi-Scale Progressive Failure Analysis and investigating what type of damage initiates; how it propagates and how it leads to failure of the structure. Process Modeling (Figure 5b) capability for powder metal includes the prediction of 3D printed global structure finite element model (FEM) net shape, residual stress, and local Grain Modeling, diffusional creep using Voronoi tessellation Mesh (2D and effect of inclusion predicts intergranular, and transgranular cracks, residual stress and strain, and surface roughness, or 3D FE Mesh, predicting surface roughness creep diffusion and intergranular and transgranular cracks, which will lead to rupture) High values of triaxial tension can trigger void nucleation and growth leading to reduced creep ductility and creep-brittle behavior. Using the elastic/plastic/creep modeling in the FEA allows the model to predict creep cracking based upon the multiaxial failure strain levels. Additive manufacturing process simulation developed by ASC includes both thermal and structural changes and is represented by coupled thermal-structural finite element (FE) analysis. A transient coupled thermo-mechanical model is used to simulate the manufacturing behavior when the fabricated part For Fracture Toughness Determination (FTD), the extended the Griffith theory is used to estimate the fracture toughness value of metallic alloys from simple uniaxial tensile tests. For Fatigue Crack Growth (FCG), the Fatigue Crack Growth rate curve (or da/dN vs. ∆K) can be generated by applying the fracture toughness value, K C (obtained from the extended Griffith theory) for the accelerated region, Paris region, and threshold regions [11].
Part qualification uses Durability and Damage Tolerance (D and DT) to assess the integrity of complex structures by performing a Multi-Scale Progressive Failure Analysis and investigating what type of damage initiates; how it propagates and how it leads to failure of the structure. Process Modeling (Figure 5b) capability for powder metal includes the prediction of 3D printed global structure finite element model (FEM) net shape, residual stress, and local Grain Modeling, diffusional creep using Voronoi tessellation Mesh (2D and effect of inclusion predicts intergranular, and trans-granular cracks, residual stress and strain, and surface roughness, or 3D FE Mesh, predicting surface roughness creep diffusion and intergranular and transgranular cracks, which will lead to rupture) High values of triaxial tension can trigger void nucleation and growth leading to reduced creep ductility and creep-brittle behavior. Using the elastic/plastic/creep modeling in the FEA allows the model to predict creep cracking based upon the multiaxial failure strain levels. Additive manufacturing process simulation developed by ASC includes both thermal and structural changes and is represented by coupled thermal-structural finite element (FE) analysis. A transient coupled thermo-mechanical model is used to simulate the manufacturing behavior when the fabricated part becomes distorted and stress is built up during manufacturing because of the repeated heating and cooling. In-situ monitoring is used to measure surface roughness with big data processing. At high temperatures, metals exhibit creep, which will lead to rupture. High values of triaxial tension can be calculated on a detail grain and grain boundary model that can trigger void nucleation and growth leading to reduced creep ductility, creep-brittle behavior, and surface roughness. Using the elastic/plastic/creep modeling in the FEA allows the model to predict creep cracking based upon the multiaxial failure strain levels. At high temperatures, metals exhibit rate-dependent (creep) deformation under constant load. Unless another failure mechanism intervenes, creep deformation will eventually lead to rupture, which is generally associated with the coalescence of voids along grain boundaries. An expression for multiaxial creep ductility is based on a mechanism of grain boundary cavitation for a power law creep material [12,13] ε Here, ε f , is the failure strain for uniaxial stress; n, is a slope, or more specifically, a material constant equivalent to one over strain rate sensitivity. The other parameters are: σ m -the ratio between the mean (hydrostatic) stress, and σ c is the equivalent (von Mises) stress.

Fracture Toughness and Fatigue Crack Growth Model
The information from a complete stress-strain curve is used to estimate the fracture toughness based on the energy method [11]. The Fracture Toughness Determination code (FTD) is a useful tool that can generate the plane strain and plane stress fracture toughness for metallic alloys by using the material static properties. In addition, it can provide material fracture toughness as a function of part thickness. In Part II, the plane strain and plane stress fracture toughness (KIC and KC) were used to generate the fatigue crack growth rate data (da/dN vs. ∆K curve). The Fatigue Crack Growth (FCG) is established to generate the whole region of the da/dN versus ∆K curve [11]. da/dN versus ∆K curve is used to predict the fatigue life and residual strength in conjunction with finite element analysis (FEA). Material residual strength capability curve (a plot of fracture stress versus half a crack length) can be generated through the extended Griffith theory [5,6]. Energy absorption rate for plastic deformation at the crack tip is calculated and used to establish a relationship between fracture stress and half critical crack length. The total energy per unit thickness absorbed in plastic straining of the material around the crack tip, U P , can be written as follows: where U F and U U are the energy absorbed per unit thickness in plastic straining of the material beyond the ultimate at the crack tip and below the ultimate stress near the crack tip, respectively. The extended energy balance equation, in terms of U F and U U , described by Equation (1), can be rewritten as follows: where U E and U S are the total available energy and energy necessary to create two new crack surfaces. g 1 = ∂U F /∂c and g 2 = ∂U U /∂c are the rates at which energy is absorbed in plastic straining beyond the ultimate stress at the crack tip and below the ultimate stress near the crack tip, respectively. The extended Griffith theory in terms of g 1 and g 2 can be rewritten as follows: where ∂U S /∂c = 2T, the work done in creating two new crack surfaces. TMg Predicts: (i) Process Map, (ii) Thermal State (heating, melting, superheated-melt, superheated-cooling, consolidation/sintering, cooling) ( Figure 6), (iii) Material State (Void, density, VOS), and (iv) Phase diagram, crystallization and composition contribution. Finite difference Zeroth-Order Model algorithm was developed towards modeling of real-time calculation/prediction of Thermal History in laser powder bed fusion (LPBF) process for both laser scanning (power and speed) and laser stationary (power) analyses [14]. TMg has been validated for Titanium [15] with respect to dynamic evolution of melt pool depth-width. TMg predicts Material State and can be used to define a dynamic Process Map that relates common manufacturing anomalies to laser power and speed. Software has been previously validated for INC-718, Ti64, SS-316L, and AlSi10Mg. TMg was also validated for Stainless Steel for an LPBF platform. Here, the dynamic process map (P-V-T envelope) and the zones of stabilities and instabilities were validated for a single track of laser moving at different laser power and scan speed (range of P: 150-700 W and V: 300-750 mm/s). The predicted zones such as balling, humping, and stable regions) were compared with the literature data [16] and were in good agreement ( Figure 7). TMg Predicts: (i) Process Map, (ii) Thermal State (heating, melting, superheated-melt, superheated-cooling, consolidation/sintering, cooling) ( Figure 6), (iii) Material State (Void, density, VOS), and (iv) Phase diagram, crystallization and composition contribution. Finite difference Zeroth-Order Model algorithm was developed towards modeling of real-time calculation/prediction of Thermal History in laser powder bed fusion (LPBF) process for both laser scanning (power and speed) and laser stationary (power) analyses [14]. TMg has been validated for Titanium [15] with respect to dynamic evolution of melt pool depth-width. TMg predicts Material State and can be used to define a dynamic Process Map that relates common manufacturing anomalies to laser power and speed. Software has been previously validated for INC-718, Ti64, SS-316L, and AlSi10Mg. TMg was also validated for Stainless Steel for an LPBF platform. Here, the dynamic process map (P-V-T envelope) and the zones of stabilities and instabilities were validated for a single track of laser moving at different laser power and scan speed (range of P: 150-700 W and V: 300-750 mm/s). The predicted zones such as balling, humping, and stable regions) were compared with the literature data [16] and were in good agreement (Figure 7).    (Figure 6), (iii) Material State (Void, density, VOS), and (iv) Phase diagram, crystallization and composition contribution. Finite difference Zeroth-Order Model algorithm was developed towards modeling of real-time calculation/prediction of Thermal History in laser powder bed fusion (LPBF) process for both laser scanning (power and speed) and laser stationary (power) analyses [14]. TMg has been validated for Titanium [15] with respect to dynamic evolution of melt pool depth-width. TMg predicts Material State and can be used to define a dynamic Process Map that relates common manufacturing anomalies to laser power and speed. Software has been previously validated for INC-718, Ti64, SS-316L, and AlSi10Mg. TMg was also validated for Stainless Steel for an LPBF platform. Here, the dynamic process map (P-V-T envelope) and the zones of stabilities and instabilities were validated for a single track of laser moving at different laser power and scan speed (range of P: 150-700 W and V: 300-750 mm/s). The predicted zones such as balling, humping, and stable regions) were compared with the literature data [16] and were in good agreement (Figure 7).

Scatter and Uncertainty Evaluation and Allowable Generation
Methods for Generic basis and Reduced Test Plan have been discussed in [17] about the need to qualify AM materials by computing A and B basis allowables similar to MMPDS [2] document. The number of required specimens for both A-and B-basis allowable determination is one hundred specimens. A total of 100 specimens from 10 heats and 10 lots. However, if test results do not fit any distribution, like Normal or Weibull, then an end-user would require 299 specimens from 10 heats and 10 lots. I have not seen any cases that the data does not fit any distractions. Therefore, in most cases, we will need 100 specimens. Please note this is required for tensile tests in order to develop yield and ultimate tensile strengths. If you have Tensile Allowables, then you need only 20 specimens for properties such as shear and compression Allowables. Reduced B-basis sampling would require the use of 20 samples, 3 heats and reduced lots. This will achieve certification/qualification virtually by computing an acceptance region across different batches/machines/process and utilizing the statistical acceptance values in qualification simulations (static, PSD) to virtually qualify the component [17]. There are three methods to qualify AM materials and parts: extensive testing, equivalence based/reduced testing for new process, and model-based (simulation) where testing is minimal [18]. We will attempt to use the model-based method. The first step would be to determine the generic basis acceptance region of the material across different batches/machines/process [6]. After that, we would utilize this acceptance region in qualification, proto-qualification, acceptance, prelaunch, and post launch validation requirements [3,18].
The Probabilistic Engine [17] is equipped with many methods including low-and high-fidelity methods such as first-order and second-order reliability methods (FORM and SORM), Advanced Mean Value, Adaptive Importance Sampling, and MCS (Monte Carlo Simulation). The approach for determination of strength allowable ( Figure 6) with reduced testing builds on existing accepted standards and practices [17]. It uses statistics from Material level testing to reverse engineer microstructure uncertainties in void (shape, size, distribution) and material strength, and stiffness properties and manufacturing variables. These uncertainties are subsequently used in generating random virtual test samples for laminated notched and un-notched specimens. The virtual samples are then used in lieu of actual test samples.
The methodology combines probabilistic methods with advanced multi-scale, multi-physics progressive failure analysis (MS-PFA) [8,9] and Bayesian statistics to reduce the number of tests needed for determination of A-and B-basis strength values.

AlSi10Mg Coin Specimen and LBFP Process
Meltpool Engineering-Thermal Prediction Validation-of Void and Effect on AlSi10Mg Mechanical Properties Figure 8 shows Thermal transport prediction of Aluminum (AlSi10Mg) Transient Thermal-State for LPBF laser melting (Laser spot 80 mm, P = 407 W and V = 1190 mm/s). This includes six process regions (heating, melting, melt-superheated, superheated-cooling, solidification/sintering and cooling). Figure 8b shows the transient thermal states for a small laser spot at different time steps. Figure 8c shows the transient void ratios.
Coatings 2020, 10, 625 11 of 23 Meltpool Engineering-Thermal Prediction Validation-of Void and Effect on AlSi10Mg Mechanical Properties Figure 8 shows Thermal transport prediction of Aluminum (AlSi10Mg) Transient Thermal-State for LPBF laser melting (Laser spot 80 mm, P = 407 W and V = 1190 mm/s). This includes six process regions (heating, melting, melt-superheated, superheated-cooling, solidification/sintering and cooling). Figure 8b shows the transient thermal states for a small laser spot at different time steps. Figure 8c shows the transient void ratios.

Experimental and Simulation Results for Porosity in AlSi10Mg
The effect of different values of laser power and speed on density of AlSi10Mg specimens and their porosity has been evaluated in [7]. Microscale porosity was simulated, and experimental data and numerical results are compared in Figure 9 for different values of laser power and speed.

Experimental and Simulation Results for Porosity in AlSi10Mg
The effect of different values of laser power and speed on density of AlSi10Mg specimens and their porosity has been evaluated in [7]. Microscale porosity was simulated, and experimental data and numerical results are compared in Figure 9 for different values of laser power and speed.  Effect of Porosity and Print Orientation on Material Properties of AlSi10Mg is discussed (Table  3). It has been noted [11] that elastic modulus changes from 7.5 × 10 4 N/mm 2 for cast AlSi10Mg to 7.29 × 10 4 N/mm 2 for AM AlSi10Mg with AM voids. Tensile and compressive strength changes from 2.10 × 10 2 N/mm 2 for cast AlSi10Mg to 1.7957 × 10 2 N/mm 2 for AM AlSi10Mg with AM voids. Poisson's ratio changes from 0.3 for cast AlSi10Mg to 0.297 for AM AlSi10Mg with AM voids. Density changes from 2670 kg/m 3 for cast AlSi10Mg to 2605 kg/m 3 for AM AlSi10Mg with AM voids.
The Structural Requirements are Tensile Properties: (i) Minimum Tensile Strength: 130 ksi; (ii) Minimum Elongation: 5%; and (iii) Minimum Yield Strength: 119 ksi. Table 3 shows the Tensile Data Related to Build Orientation: (a) oxygen content, and (b) scatter in mechanical properties (UTS, YS, El%, and RA). Figure 10 shows the predicted stress-strain curve in XY, YZ, and XZ directions vs. test observations.

Tensile Data Related to Build Orientation.
Effect of Porosity and Print Orientation on Material Properties of AlSi10Mg is discussed (Table 3). It has been noted [11] that elastic modulus changes from 7.5 × 10 4 N/mm 2 for cast AlSi10Mg to 7.29 × 10 4 N/mm 2 for AM AlSi10Mg with AM voids. Tensile and compressive strength changes from 2.10 × 10 2 N/mm 2 for cast AlSi10Mg to 1.7957 × 10 2 N/mm 2 for AM AlSi10Mg with AM voids. Poisson's ratio changes from 0.3 for cast AlSi10Mg to 0.297 for AM AlSi10Mg with AM voids. Density changes from 2670 kg/m 3 for cast AlSi10Mg to 2605 kg/m 3 for AM AlSi10Mg with AM voids.    Table 3 shows the Tensile Data Related to Build Orientation: (a) oxygen content, and (b) scatter in mechanical properties (UTS, YS, El%, and RA). Figure 10 shows the predicted stress-strain curve in XY, YZ, and XZ directions vs. test observations.    Table 3 shows the Tensile Data Related to Build Orientation: (a) oxygen content, and (b) scatter in mechanical properties (UTS, YS, El%, and RA). Figure 10 shows the predicted stress-strain curve in XY, YZ, and XZ directions vs. test observations.    Table 3 shows the Tensile Data Related to Build Orientation: (a) oxygen content, and (b) scatter in mechanical properties (UTS, YS, El%, and RA). Figure 10 shows the predicted stress-strain curve in XY, YZ, and XZ directions vs. test observations.  Table 3 shows the Tensile Data Related to Build Orientation: (a) oxygen content, and (b) scatter in mechanical properties (UTS, YS, El%, and RA). Figure 10 shows the predicted stress-strain curve in XY, YZ, and XZ directions vs. test observations.  Figure 11 shows Variations of Test Values of Strength of AlSi10Mg. Figure 12a shows Allowable (A-B) basis value prediction-compared with test. A-Basis is defined as a strength value at which only 1 in 100 specimens will fail with a 95% confidence level. B-Basis is a strength value at which only 10 in 100 specimens will fail with a 95% confidence level. The following formula is used to determine a A-and B-basis value for normal distribution: B = X -kB(s), where X is the arithmetical Mean, k is a constant (called the tolerance factor) depending on the number of specimens, n, and s is the standard deviation. Figure 12b shows the Sensitivity Analysis of Strength of AlSi10Mg to Variations of Material Properties, indicating that increasing the void and reducing material shear strength have positive and negative sensitivity, respectively. Positive sensitivity to void ratio means that increasing the void ratio has a negative effect on strength. Negative sensitivity to shear strengths means that increasing these material properties results in higher strength.   Figure 12a shows Allowable (A-B) basis value prediction-compared with test. A-Basis is defined as a strength value at which only 1 in 100 specimens will fail with a 95% confidence level. B-Basis is a strength value at which only 10 in 100 specimens will fail with a 95% confidence level. The following formula is used to determine a Aand B-basis value for normal distribution: B = X -k B (s), where X is the arithmetical Mean, k is a constant (called the tolerance factor) depending on the number of specimens, n, and s is the standard deviation. Figure 12b shows the Sensitivity Analysis of Strength of AlSi10Mg to Variations of Material Properties, indicating that increasing the void and reducing material shear strength have positive and negative sensitivity, respectively. Positive sensitivity to void ratio means that increasing the void ratio has a negative effect on strength. Negative sensitivity to shear strengths means that increasing these material properties results in higher strength.  Figure 11 shows Variations of Test Values of Strength of AlSi10Mg. Figure 12a shows Allowable (A-B) basis value prediction-compared with test. A-Basis is defined as a strength value at which only 1 in 100 specimens will fail with a 95% confidence level. B-Basis is a strength value at which only 10 in 100 specimens will fail with a 95% confidence level. The following formula is used to determine a A-and B-basis value for normal distribution: B = X -kB(s), where X is the arithmetical Mean, k is a constant (called the tolerance factor) depending on the number of specimens, n, and s is the standard deviation. Figure 12b shows the Sensitivity Analysis of Strength of AlSi10Mg to Variations of Material Properties, indicating that increasing the void and reducing material shear strength have positive and negative sensitivity, respectively. Positive sensitivity to void ratio means that increasing the void ratio has a negative effect on strength. Negative sensitivity to shear strengths means that increasing these material properties results in higher strength.    Table 4 shows Fracture toughness of AlSi10Mg [18] for three different print orientations. Figure  13 Shows the Fracture toughness of AlSi10Mg printed in XY, XZ and YZ print orientation in the table. The generated stress-strain curve for each orientation due to void is used as input to FTD.   Table 4 shows Fracture toughness of AlSi10Mg [18] for three different print orientations. Figure 13 Shows the Fracture toughness of AlSi10Mg printed in XY, XZ and YZ print orientation in the table. The generated stress-strain curve for each orientation due to void is used as input to FTD.

Print Orientation Effect on Tensile Strength and Strain
The effects of heat treatment on the investigated SLM parts are attributed to the formation of precipitates in the material matrix, as well as the altering of other micro structural features, i.e., phase volume fraction, grain size and morphology, while the build orientation has direct influence on the damage evolution under loading. A part's building orientation during SLM influences its cooling rate (due to the part's aspect ratio), and thus encumbered microstructure, while the final orientation of deposited layers (which depend on build direction) impacts part strength in various loading   Table 4 shows Fracture toughness of AlSi10Mg [18] for three different print orientations. Figure  13 Shows the Fracture toughness of AlSi10Mg printed in XY, XZ and YZ print orientation in the table. The generated stress-strain curve for each orientation due to void is used as input to FTD.  Table 4 shows Fracture toughness of AlSi10Mg [18] for three different print orientations. Figure  13 Shows the Fracture toughness of AlSi10Mg printed in XY, XZ and YZ print orientation in the table. The generated stress-strain curve for each orientation due to void is used as input to FTD.  Table 4 shows Fracture toughness of AlSi10Mg [18] for three different print orientations. Figure  13 Shows the Fracture toughness of AlSi10Mg printed in XY, XZ and YZ print orientation in the table. The generated stress-strain curve for each orientation due to void is used as input to FTD. The effects of heat treatment on the investigated SLM parts are attributed to the formation of precipitates in the material matrix, as well as the altering of other micro structural features, i.e., phase volume fraction, grain size and morphology, while the build orientation has direct influence on the damage evolution under loading. A part's building orientation during SLM influences its cooling rate (due to the part's aspect ratio), and thus encumbered microstructure, while the final orientation of deposited layers (which depend on build direction) impacts part strength in various loading directions. Table 5 shows typical RT Tensile Properties for EBM Ti-6Al-4V. The probabilistic sensitivities in this section will show that in order for the next-generation technology to improve the strength of 3D printed materials, they must control the porosity volume fraction and orientation of voids. This 3D EBM material is shown to be over 99.99% reliable. Scatter of 3D printed Ti-6Al-4V mechanical properties (Yield, Ultimate, Elongation, and Reduction of Area) have been observed at room and high temperature (RT/HT). The MCQ Code prediction capabilities are used to show variation in Stress-Strain Curves Characteristic Points and Residual Stress due to porosity (void/defect) shape and size and orientation similar to those found after the EBM 3D printed Ti-6Al-4V process. Figure 14 also shows the variation of strength with respect to manufacturing process parameters at RT and HT (700 • C). The samples were fabricated horizontally and vertically in multiple directions to find the effect on the mechanical properties such as UTS, YS, and %EL. The vertical and horizontal rod specimens are 2 inches in length and 0.25 in diameter (Table 6).      MCQ software and methods was used to predict A/B basis allowables including the material mechanical properties (stiffness, strength) at different temperatures, and probabilistic Sensitivity Analysis with respect to Process defects.

Scatter of Titanium Properties at Room (RT) and High Temperature (HT)
MCQ predictions were validated with Ti-6Al-4V to be able to predict static and fatigue DMLS printed metal properties and allowables at room and high temperature. The static properties were predicted by mixing Ti6Al4V base metal properties stress-strain curve prediction considering defects (void) percentages and compared to test (Figure 15) of 3D printed Direct Metal Laser Sintered (DMLS) material using nano-based inclusion/defects algorithm: A nano-mechanics-based material modeling tool was used to predict stress-strain curves with effect of air particles as voids. The defect volume percentage, shape (ellipsoid shown), and aspect ratios are used as inputs to predict stiffness and strength in all directions. Output properties can be isotropic, orthotropic, or anisotropic. The Wrought with Air Particles is the simulation curve and the Laser Engineered Net Shaping (LENS) is the tested printed material. The SS curve was idealized in black in the top right of Figure 15 to be able to predict fracture toughness vs thickness. The plane strain fracture toughness is then fed into computations for fatigue crack growth determinations and the results of the MCQ metals prediction (FCG) are compared with test Ti6Al4V DMLS Milled. Furthermore, the da/dN vs. dG curve is used as input to an FE model to determine the fatigue (S-N) life of the part. A separate parameter accounted for additional observed surface roughness. The S-N prediction matched the DMLS As Built test data, which is a reduced life compared to milled specimens. The FTD and FCG process is the result of two theoretically based breakthrough methodologies for metals that compute fracture/crack growth properties from stress-strain curves, as shown in Figure 16. The capability has been accepted by ASTM [19].
an FE model to determine the fatigue (S-N) life of the part. A separate parameter accounted for additional observed surface roughness. The S-N prediction matched the DMLS As Built test data, which is a reduced life compared to milled specimens. The FTD and FCG process is the result of two theoretically based breakthrough methodologies for metals that compute fracture/crack growth properties from stress-strain curves, as shown in Figure 16. The capability has been accepted by ASTM [19].

Material Modeling-Source of Scatter and Uncertainties for EBM Process
The input Properties for Ti6Al4V and Inclusions (Table 7a-c) and baseline Stress-Strain ( Figure 17) show that we utilize the Wrought properties of Ti-6Al-4V, add inclusions, their shape (cylindrical, ellipsoidal, etc.), size ratios (length, width and height), and volume fraction to predict strength.  The input Properties for Ti6Al4V and Inclusions (Table 7a-c) and baseline Stress-Strain ( Figure  17) show that we utilize the Wrought properties of Ti-6Al-4V, add inclusions, their shape (cylindrical, ellipsoidal, etc.), size ratios (length, width and height), and volume fraction to predict strength.  Test observation showed that print direction will affect stiffness, and strength. Void shape and size are key in determining properties. Scatter Coefficient of Variation (COV) prediction was performed with acceptable results at room and high temperature. After random variations of the inputs (Table 7), a response surface is formed and used in a probabilistic simulation (Figure 18), which computes a CDF ( Figure 18a) and probabilistic sensitivities (Figure 18b) for Yield Strength, Ultimate Strength, and %Elongation. Figure 19 shows SS Curve variations ( Figure 19a) and zoomed in to show several yield strengths ( Figure 19b) and UTS and Elongations (Figure 19c). The percentage differences for RT and HT allowables predictions are under 10% for mean and standard deviation predictions (Table 9). With knowledge of the CDF and design requirements in Table 8 The input Properties for Ti6Al4V and Inclusions (Table 7a-c) and baseline Stress-Strain ( Figure  17) show that we utilize the Wrought properties of Ti-6Al-4V, add inclusions, their shape (cylindrical, ellipsoidal, etc.), size ratios (length, width and height), and volume fraction to predict strength.  Test observation showed that print direction will affect stiffness, and strength. Void shape and size are key in determining properties. Scatter Coefficient of Variation (COV) prediction was performed with acceptable results at room and high temperature. After random variations of the inputs (Table 7), a response surface is formed and used in a probabilistic simulation (Figure 18), which computes a CDF ( Figure 18a) and probabilistic sensitivities (Figure 18b) for Yield Strength, Ultimate Strength, and %Elongation. Figure 19 shows SS Curve variations ( Figure 19a) and zoomed in to show several yield strengths ( Figure 19b) and UTS and Elongations (Figure 19c). The percentage differences for RT and HT allowables predictions are under 10% for mean and standard deviation predictions (Table 9). With knowledge of the CDF and design requirements in Table 8 The input Properties for Ti6Al4V and Inclusions (Table 7a-c) and baseline Stress-Strain ( Figure  17) show that we utilize the Wrought properties of Ti-6Al-4V, add inclusions, their shape (cylindrical, ellipsoidal, etc.), size ratios (length, width and height), and volume fraction to predict strength.  Test observation showed that print direction will affect stiffness, and strength. Void shape and size are key in determining properties. Scatter Coefficient of Variation (COV) prediction was performed with acceptable results at room and high temperature. After random variations of the inputs (Table 7), a response surface is formed and used in a probabilistic simulation (Figure 18), which computes a CDF ( Figure 18a) and probabilistic sensitivities (Figure 18b) for Yield Strength, Ultimate Strength, and %Elongation. Figure 19 shows SS Curve variations ( Figure 19a) and zoomed in to show several yield strengths ( Figure 19b) and UTS and Elongations (Figure 19c). The percentage differences for RT and HT allowables predictions are under 10% for mean and standard deviation predictions (Table 9). With knowledge of the CDF and design requirements in Table 8 (Min YS119 ksi, Min UTS130 ksi, and Min 5% Elongation), we can say that this 3D printed material is over 99.99% reliable for all requirements. The input Properties for Ti6Al4V and Inclusions (Table 7a-c) and baseline Stress-Strain ( Figure  17) show that we utilize the Wrought properties of Ti-6Al-4V, add inclusions, their shape (cylindrical, ellipsoidal, etc.), size ratios (length, width and height), and volume fraction to predict strength.  Test observation showed that print direction will affect stiffness, and strength. Void shape and size are key in determining properties. Scatter Coefficient of Variation (COV) prediction was performed with acceptable results at room and high temperature. After random variations of the inputs (Table 7), a response surface is formed and used in a probabilistic simulation (Figure 18), which computes a CDF ( Figure 18a) and probabilistic sensitivities (Figure 18b) for Yield Strength, Ultimate Strength, and %Elongation. Figure 19 shows SS Curve variations (Figure 19a) and zoomed in to show several yield strengths (Figure 19b) and UTS and Elongations (Figure 19c). The percentage differences for RT and HT allowables predictions are under 10% for mean and standard deviation predictions (Table 9). With knowledge of the CDF and design requirements in Table 8 (Min YS119 ksi, Min UTS130 ksi, and Min 5% Elongation), we can say that this 3D printed material is over 99.99% reliable for all requirements. Test observation showed that print direction will affect stiffness, and strength. Void shape and size are key in determining properties. Scatter Coefficient of Variation (COV) prediction was performed with acceptable results at room and high temperature. After random variations of the inputs (Table 7), a response surface is formed and used in a probabilistic simulation (Figure 18), which computes a CDF ( Figure 18a) and probabilistic sensitivities (Figure 18b) for Yield Strength, Ultimate Strength, and %Elongation. Figure 19 shows SS Curve variations (Figure 19a) and zoomed in to show several yield strengths (Figure 19b) and UTS and Elongations (Figure 19c). The percentage differences for RT and HT allowables predictions are under 10% for mean and standard deviation predictions (Table 8). With knowledge of the CDF and design requirements in Table 9 (Min YS119 ksi, Min UTS130 ksi, and Min 5% Elongation), we can say that this 3D printed material is over 99.99% reliable for all requirements.

Conclusions
AM Part qualification requires Mechanical Strength and scatter measurement, and establishment of fracture control plan. The ICME Material Characterization and Qualification (MCQ) software material model prediction capabilities are used to predict: (a) Material Allowables, Stress-Strain Curves, and Residual Stress. The probabilistic simulation computes (i) the probabilistic sensitivities for Yield Strength, Ultimate Strength, and %Elongation as well as A and B basis allowables; (ii) the Fracture Control Plan for fracture toughness determination, and (iii) fatigue crack growth vs. stress intensity of the As-Built 3D printed material.
As part of case study effort, two AM modalities were chosen: (1) LPBF manufacturing of AlSi10Mg, and (2) EBM Manufacturing of Ti-6Al-4V demonstrated for Part Quality assurance. The latter component ensured that all physical and mechanical properties met or exceeded requirements. Scatter and Uncertainty in Material mechanical properties were predicted and compared with test data. A-B Basis allowables were generated based on reduced testing technique. As part of the fracture control plan, fracture and fatigue properties were computed and compared with test data, and found to be in a good agreement with the data.