Manufacturing of Continuous Carbon Fiber Reinforced Aluminum by Spark Plasma Sintering

: In the ﬁeld of metal matrix composites (MMC), spark plasma sintering (SPS) technique has been used so far for the manufacture of particle, whisker and short-ﬁber reinforced alloys. In this work, SPS technique is employed for the ﬁrst time to produce continuous ﬁber reinforced light metals. For this purpose, metal matrix composite prepregs with aluminum as a surface coating on carbon ﬁber textiles are manufactured by twin arc wire spraying and subsequently consolidated by SPS in the semi-solid temperature range of the alloy. Shear thinning rheological behavior of the metal alloy at temperatures between solidus and liquidus enables the inﬁltration of ﬁber rovings under reduced forming loads. SPS o ﬀ ered a better controlled and more e ﬃ cient heat transfer in the green body and faster consolidation cycles in comparison with alternative densiﬁcation methods. Fully densiﬁed samples with no porosity proved the suitability of SPS for densiﬁcation of MMC with a remarkable sti ﬀ ness increase in comparison with samples densiﬁed by thixoforging, an alternative consolidation method. However, the pulse activated sintering process leads to a quite strong ﬁber / matrix adhesion with evidence of aluminum carbide formation.


Introduction
Aluminum has become the preferred structural material for a myriad of applications in the fields of ground transportation and aeronautics because of its low density in comparison with carbon steel. Nevertheless, specific demands of certain components require the use of alternative lightweight materials with higher stiffness and targeted thermo-physical properties. Due to this reason, metal matrix composites (MMC) have been in focus of research over the last 50 years. By adequate selection of reinforcing phase and composite architecture, different objectives can be achieved by the substitution of conventional materials by MMC components such as, Young's modulus increase, reduction of thermal elongation and creep resistance increase [1]. For niche applications in sectors of low pricing pressure, such as aerospace, different material solutions based on ceramic fiber (SiC, Al 2 O 3 ) reinforced light metals have been developed since the 1980s [2]. However, for the establishment of fiber reinforced light metals in application fields with tough cost targets, as ground transportation or mechanical engineering, low-priced raw materials and economically viable manufacturing processes are required.
The search for synergies between outstanding mechanical properties of low-priced polyacrylonitrile-based carbon fibers and the low density of aluminum has attracted wide attention from academia and industry. However, the chemical compatibility of the matrix and reinforcing phase of this material system is still today an unresolved technical hurdle. The uncontrolled growth of aluminum carbide crystals, which are formed at the C f /Al interface during high-temperature exposures, has been proven to impair mechanical properties of such composites. Several publications have contributed to a better understanding of growth mechanisms and implications of interfacial Al 4 C 3 nanocrystals for the micro-and macro mechanical properties of C f /Al [3][4][5][6][7]. According to the published literature about this topic, the compatibility of C f /Al interface can be optimized by different strategies: • Deposition of thin ceramic or metallic interlayers at the interface [8][9][10]; • Functionalization of fiber surface; targeted selection of carbon fibers with suitable surface topography [11]; • Selection of aluminum alloys with certain levels of alloying elements, which contribute to inhibition of Al 4 C 3 growth [12,13]; • Optimization of manufacturing parameters for the reduction of thermal exposure.
The last two strategies are especially interesting from the point of view of cost effectiveness, because their application is linked with no further manufacturing steps. For their implementation, a wide knowledge about the most suitable manufacturing parameters, concerning interfacial properties optimization for different aluminum alloys, is necessary. However, and according to the state of the art previous to this publication, this study has not been conducted so far.
Considering published literature, carbide growth and therefore interfacial properties are very sensitive to minor gradients of temperature during shaping and post-treatment [6]. Therefore, it is necessary to operate with a very accurate control of processing parameters for a decent study on optimization of time-temperature progression.
Spark plasma sintering (SPS), which has been investigated in the recent years not only for the manufacturing of high-performance ceramics but also for consolidation of particle [14,15], carbon nanotube [16] and short fiber reinforced light metals [17,18], is a technically feasible tool to perform this task. The aim of this work is conducting for first time a feasibility study on the SPS consolidation of continuously reinforced aluminum matrix composites. In order to compare the obtained results of samples densified by SPS with an alternative method, MMC reference samples are manufactured by thixoforging with a hydraulic press from the same raw materials.

Materials and Methods
For the study on SPS consolidation of continuous fiber reinforced aluminum following raw materials were employed: • Reinforcement: Carbon fiber woven fabrics in plain weave binding with an areal weight of 160 g/m 2 from HT 200 tex 3k carbon rovings • Matrix: Wires of 1.6 mm diameter supplied by Drahtwerk Elisental (Neuenrade, Germany) of aluminum alloys AlSi1MgMn, AlSi5, AlSi7Mg, and AlSi10Mg. Chemical compositions of every alloy are shown in Table 1. The manufacturing process chain followed in this study is summarized in Figure 1. Woven fabrics were initially cut into sheets, which were coated with the metallic matrix by means of thermal spraying. The resulting MMC prepregs were consolidated to C f /Al samples by two different methods: SPS and thixoforging. MMC prepregs consisting of metallized carbon fiber fabrics were manufactured by means of twin wire arc spraying. This spraying technique consists of the continuous mechanical feeding of two metallic wires with the same chemical composition, parallel and with equal speed, into a spray gun. As the wires are electrically charged with opposing polarity, an electric arc is generated between the tips of the wires. The resulting heat melts the metallic feedstock. Molten particles are atomized and accelerated towards the substrate by compressed air flow. A twin wire arc torch Sparc 400 (GTV Verschleißschutz GmbH, Luckenbach, Germany) was used in this study. The torch was mounted on a robot arm, which followed a meander trajectory with a speed of 400 mm/s. The robot arm repeated six times the same trajectory on both sides of the woven fabric with a wire feed speed of 3.9 m/min and an output voltage of 36 V for sustaining the electric arc. After the thermal spraying process, the carbon fiber fabrics are pre-infiltrated by aluminum as shown in Figure 2. The resulting coated fabrics were cut in different geometries to fit the die dimensions. In the case of the prepregs for SPS experiments, coated fabrics were cut in circles with a diameter of 49 mm. The SPS graphite die was covered with graphite foil as a release agent layer and eight stacked prepregs were additionally covered with two graphite discs at the top and at the bottom. The fiber prepregs MMC prepregs consisting of metallized carbon fiber fabrics were manufactured by means of twin wire arc spraying. This spraying technique consists of the continuous mechanical feeding of two metallic wires with the same chemical composition, parallel and with equal speed, into a spray gun. As the wires are electrically charged with opposing polarity, an electric arc is generated between the tips of the wires. The resulting heat melts the metallic feedstock. Molten particles are atomized and accelerated towards the substrate by compressed air flow. A twin wire arc torch Sparc 400 (GTV Verschleißschutz GmbH, Luckenbach, Germany) was used in this study. The torch was mounted on a robot arm, which followed a meander trajectory with a speed of 400 mm/s. The robot arm repeated six times the same trajectory on both sides of the woven fabric with a wire feed speed of 3.9 m/min and an output voltage of 36 V for sustaining the electric arc. After the thermal spraying process, the carbon fiber fabrics are pre-infiltrated by aluminum as shown in Figure 2. MMC prepregs consisting of metallized carbon fiber fabrics were manufactured by means of twin wire arc spraying. This spraying technique consists of the continuous mechanical feeding of two metallic wires with the same chemical composition, parallel and with equal speed, into a spray gun. As the wires are electrically charged with opposing polarity, an electric arc is generated between the tips of the wires. The resulting heat melts the metallic feedstock. Molten particles are atomized and accelerated towards the substrate by compressed air flow. A twin wire arc torch Sparc 400 (GTV Verschleißschutz GmbH, Luckenbach, Germany) was used in this study. The torch was mounted on a robot arm, which followed a meander trajectory with a speed of 400 mm/s. The robot arm repeated six times the same trajectory on both sides of the woven fabric with a wire feed speed of 3.9 m/min and an output voltage of 36 V for sustaining the electric arc. After the thermal spraying process, the carbon fiber fabrics are pre-infiltrated by aluminum as shown in Figure 2. The resulting coated fabrics were cut in different geometries to fit the die dimensions. In the case of the prepregs for SPS experiments, coated fabrics were cut in circles with a diameter of 49 mm. The SPS graphite die was covered with graphite foil as a release agent layer and eight stacked prepregs were additionally covered with two graphite discs at the top and at the bottom. The fiber prepregs The resulting coated fabrics were cut in different geometries to fit the die dimensions. In the case of the prepregs for SPS experiments, coated fabrics were cut in circles with a diameter of 49 mm. The SPS graphite die was covered with graphite foil as a release agent layer and eight stacked prepregs were additionally covered with two graphite discs at the top and at the bottom. The fiber prepregs were then consolidated to discs of 49 mm diameter with SPS equipment by FCT Systeme (Rauenstein, Germany). The pulse condition used in this study was 8:2, relating the first number to the time ON and the second to the time OFF (both magnitudes measured in ms). An initial axial pressure of 5 MPa and a preheating of 350 • C were applied to close the gaps between layers and to homogenize the temperature at a value under the liquidus temperature of the alloy. According to the published literature, this value of preheating temperature does not lead to aluminum carbide formation at the fiber/matrix interface [6]. Finally, temperature and pressure were raised to their target values. Three different densification temperatures of the semi-solid temperature range were chosen for every alloy. Furthermore, two different axial pressures-7.5 and 10 MPa-for each densification temperature were investigated. Depending on the alloy, the densification temperature varied between 585 • C and 650 • C. Figure 3 shows exemplary a densification cycle with a densification temperature of 605 • C and an applied axial pressure of 10 MPa.
Ceramics 2020, 3, 24 268 were then consolidated to discs of 49 mm diameter with SPS equipment by FCT Systeme (Rauenstein, Germany). The pulse condition used in this study was 8:2, relating the first number to the time ON and the second to the time OFF (both magnitudes measured in ms). An initial axial pressure of 5 MPa and a preheating of 350 °C were applied to close the gaps between layers and to homogenize the temperature at a value under the liquidus temperature of the alloy. According to the published literature, this value of preheating temperature does not lead to aluminum carbide formation at the fiber/matrix interface [6]. Finally, temperature and pressure were raised to their target values. Three different densification temperatures of the semi-solid temperature range were chosen for every alloy. Furthermore, two different axial pressures-7.5 and 10 MPa-for each densification temperature were investigated. Depending on the alloy, the densification temperature varied between 585 °C and 650 °C. Figure 3 shows exemplary a densification cycle with a densification temperature of 605 °C and an applied axial pressure of 10 MPa. For the thixoforging densification experiments, coated fabrics were cut into rectangular sheets of 120 × 150 mm 2 . Eight prepregs layers were laminated and wrapped with a steel foil of 0.1 mm thickness to avoid loss of liquid fraction of the alloy during densification. In order to enable an easy removal of MMC plates after densification, the interior side of steel foil was impregnated with EKamold ® boron nitride suspension (3M, Minnesota, USA) as release agent. Prepreg packages were then heated by a propane-powered infrared radiator and transferred to a hydraulic press Type HPS-S 1000 kN by Schuler Hydrap (Plüderhausen, Germany). Target values of pressing force and stroke speed were set to 1000 kN (~67 MPa) and 6 mm/s respectively.
In order to set appropriate densification temperatures for every alloy, melting properties of metal wires were characterized by differential scanning calorimetry (DSC). This method enables the determination of both, the liquidus and solidus temperatures and the temperature dependence of liquid phase content of metals. The DSC tests of this study were conducted with the thermal analyzer DSC822e by Mettler Toledo (Columbus, USA). The DSC tests started with a fast heating rate of 20 K/min from room temperature to 500 °C followed by two different heating rates of 2 and 5 K/min up to 700 °C. The evaluation of the DSC curves to determine the liquid phase fraction as a function of temperature is based on the integration of the area between curve and baseline according to the standard DIN 51004 [19].
MMC samples of each alloy were consolidated at three different processing temperatures within temperature range of semi-solid state. The consolidation temperatures, which were selected for this study considering results of DSC analysis, are shown in Table 2. There are different reasons for For the thixoforging densification experiments, coated fabrics were cut into rectangular sheets of 120 × 150 mm 2 . Eight prepregs layers were laminated and wrapped with a steel foil of 0.1 mm thickness to avoid loss of liquid fraction of the alloy during densification. In order to enable an easy removal of MMC plates after densification, the interior side of steel foil was impregnated with EKamold ® boron nitride suspension (3M, Minnesota, USA) as release agent. Prepreg packages were then heated by a propane-powered infrared radiator and transferred to a hydraulic press Type HPS-S 1000 kN by Schuler Hydrap (Plüderhausen, Germany). Target values of pressing force and stroke speed were set to 1000 kN (~67 MPa) and 6 mm/s respectively.
In order to set appropriate densification temperatures for every alloy, melting properties of metal wires were characterized by differential scanning calorimetry (DSC). This method enables the determination of both, the liquidus and solidus temperatures and the temperature dependence of liquid phase content of metals. The DSC tests of this study were conducted with the thermal analyzer DSC822e by Mettler Toledo (Columbus, USA). The DSC tests started with a fast heating rate of 20 K/min from room temperature to 500 • C followed by two different heating rates of 2 and 5 K/min up to 700 • C. The evaluation of the DSC curves to determine the liquid phase fraction as a function of temperature is based on the integration of the area between curve and baseline according to the standard DIN 51004 [19].
MMC samples of each alloy were consolidated at three different processing temperatures within temperature range of semi-solid state. The consolidation temperatures, which were selected for this study considering results of DSC analysis, are shown in Table 2. There are different reasons for operating under the liquidus line: impeding loss of metal liquid phase during pressing; inhibition of reaction products formation at the interface; reduction of residual stresses; and shrinkage. This manufacturing route, based on semi-solid consolidation of thermally sprayed prepregs, has been previously investigated with alternative consolidation methods, as for instance hydraulic pressing [20][21][22]. The MMC samples were afterwards characterized with respect to Young's modulus by resonance frequency method (IMCE, Belgium) and with respect to flexural strength by static three-point bending tests according to the standard DIN-EN-658-3 "Advanced technical ceramics-Mechanical properties of ceramic composites at room temperature" on a universal testing machine Z100 (Zwick GmbH & Co. KG., Ulm, Germany). The above-mentioned standard was chosen because of the lack of a standard for fiber reinforced metals. SPS densified samples were mechanized by means of waterjet cutting as shown in Figure 4. MMC samples manufactured by thixoforming were cut with a SiC cutting disc. The ratio between sample thickness and supports distances was fixed at a value of 12 for all tests. The setup of the bending test is shown in Figure 4.
Ceramics 2020, 3, 24 269 reaction products formation at the interface; reduction of residual stresses; and shrinkage. This manufacturing route, based on semi-solid consolidation of thermally sprayed prepregs, has been previously investigated with alternative consolidation methods, as for instance hydraulic pressing [20][21][22]. The MMC samples were afterwards characterized with respect to Young ś modulus by resonance frequency method (IMCE, Belgium) and with respect to flexural strength by static threepoint bending tests according to the standard DIN-EN-658-3 "Advanced technical ceramics-Mechanical properties of ceramic composites at room temperature" on a universal testing machine Z100 (Zwick GmbH & Co. KG., Ulm, Germany). The above-mentioned standard was chosen because of the lack of a standard for fiber reinforced metals. SPS densified samples were mechanized by means of waterjet cutting as shown in Figure 4. MMC samples manufactured by thixoforming were cut with a SiC cutting disc. The ratio between sample thickness and supports distances was fixed at a value of 12 for all tests. The setup of the bending test is shown in Figure 4. The densities of consolidated samples were determined with an analytical balance (Kern ABS, Germany) using the Archimedes principle. The fiber volume fractions were calculated from the results of the density measurements, using the general rule of mixtures of fiber reinforced materials. (1) where , , : densities of composite, matrix and dispersed phase respectively; , : volume fraction of matrix and dispersed phase respectively. The densities of consolidated samples were determined with an analytical balance (Kern ABS, Germany) using the Archimedes principle. The fiber volume fractions were calculated from the results of the density measurements, using the general rule of mixtures of fiber reinforced materials.
where ρ c , ρ m , ρ f : densities of composite, matrix and dispersed phase respectively; v m , v f : volume fraction of matrix and dispersed phase respectively.

Thermal Characterization of Aluminium Alloys
The results of the liquidus and solidus temperatures for each heating rate, according to the evaluation of the DSC curves, are shown in Table 3. With regard to the solidus temperatures, there are deviations of maximum 5 K comparing both heating rates. The differences of liquidus temperatures for both heating rates achieve a maximal value of 8 K. It is a well-known fact that increments of heating rates lead to deviations of DSC curves, which directly influence the values of liquidus and solidus temperatures in this case.  Figure 5 shows the temperature dependence of liquid phase content for the investigated samples. The curve slopes are completely different for each alloy. In the case of the casting alloy AlSi10Mg, the inclination of the curve is very pronounced, especially in the range of 10-80% liquid phase content. A similar behavior can be observed for the wrought alloy AlSi1MgMn above 10% liquid phase content. Therefore, prepregs sprayed with these two alloys need to be handled with a very accurate control of processing temperatures in order to reach suitable liquid phase contents for semi-solid shaping. On the other side, the alloys AlSi5 and AlSi7Mg exhibit lower gradients, enabling their processing in semi-solid state.

Thermal Characterization of Aluminium Alloys
The results of the liquidus and solidus temperatures for each heating rate, according to the evaluation of the DSC curves, are shown in Table 3. With regard to the solidus temperatures, there are deviations of maximum 5 K comparing both heating rates. The differences of liquidus temperatures for both heating rates achieve a maximal value of 8 K. It is a well-known fact that increments of heating rates lead to deviations of DSC curves, which directly influence the values of liquidus and solidus temperatures in this case. Figure 5 shows the temperature dependence of liquid phase content for the investigated samples. The curve slopes are completely different for each alloy. In the case of the casting alloy AlSi10Mg, the inclination of the curve is very pronounced, especially in the range of 10-80% liquid phase content. A similar behavior can be observed for the wrought alloy AlSi1MgMn above 10% liquid phase content. Therefore, prepregs sprayed with these two alloys need to be handled with a very accurate control of processing temperatures in order to reach suitable liquid phase contents for semi-solid shaping. On the other side, the alloys AlSi5 and AlSi7Mg exhibit lower gradients, enabling their processing in semi-solid state.

SPS Consolidation of Samples
In general terms, MMC prepregs from the different aluminum alloys employed in this study were successfully densified in the semi-solid state temperature range of each alloy. Fiber fabrics were infiltrated by the metallic matrix with nearly no signs of porosity, as observed in Figure 6. The only exception to this behavior are the fiber prepregs sprayed with the cast alloy AlSi10Mg, which already

SPS Consolidation of Samples
In general terms, MMC prepregs from the different aluminum alloys employed in this study were successfully densified in the semi-solid state temperature range of each alloy. Fiber fabrics were Ceramics 2020, 3 271 infiltrated by the metallic matrix with nearly no signs of porosity, as observed in Figure 6. The only exception to this behavior are the fiber prepregs sprayed with the cast alloy AlSi10Mg, which already showed a particular melting behavior in the DSC analysis. The extremely high sensitivity of liquid phase content to minor temperature variations (69% increase of liquid phase content between 570 and 580 • C) hampers presumably the consolidation of fabrics metallized with this alloy, leading to the formation of numerous infiltration defects, as observed in Figure 6.
showed a particular melting behavior in the DSC analysis. The extremely high sensitivity of liquid phase content to minor temperature variations (69% increase of liquid phase content between 570 and 580 °C) hampers presumably the consolidation of fabrics metallized with this alloy, leading to the formation of numerous infiltration defects, as observed in Figure 6.
According to conducted density measurements, fiber volume content of the samples fluctuates between 45% and 54% (see Table 4). An increase of consolidation temperature and axial pressure leads to slightly higher values of fiber volume content. The reason for that is the missing small amount of liquid phase, which is pressed out of the die due to the low viscosity of the metal. Although these values are not atypically elevated for woven reinforced composites, the apparent local fiber volume content around the fiber rovings is too high for an optimal fiber/matrix stress transfer. Distances between single filaments are in some cases inexistent, as shown in the lower images of Figure 6.

Mechanical Characterization
The values of bending strength and Young ś modulus of SPS consolidated MMC samples for optimal densification parameters are given in Figure 7. For comparison purposes, the mechanical properties of MMC samples from identical prepregs consolidated by thixoforging process with hydraulic press are shown in Figure 8. Although raw materials and prepreg manufacturing process were the same in both cases, the differences of mechanical properties for both groups of samples are remarkable. SPS consolidated samples exhibit much higher stiffness and lower bending strength in comparison with MMC samples manufactured by alternative consolidation methods.
It is noticeable that, in the case of samples consolidated by SPS, differences of bending strength between each material system are minor. All bending strength values of these samples are higher than 150 MPa and lower than 165 MPa. The reason for his behavior is presumably, that failure mechanisms of SPS consolidated samples are strongly dominated by the elevated interfacial bonding strength. As observed in the failure surface (Figure 9, left image), SPS samples show a brittle behavior without signs of crack deflection, pull-out morphology or fiber debonding. This fact indicates a strong fiber/matrix adhesion, which would be the limiting factor of the composite under flexural stress. This According to conducted density measurements, fiber volume content of the samples fluctuates between 45% and 54% (see Table 4). An increase of consolidation temperature and axial pressure leads to slightly higher values of fiber volume content. The reason for that is the missing small amount of liquid phase, which is pressed out of the die due to the low viscosity of the metal. Although these values are not atypically elevated for woven reinforced composites, the apparent local fiber volume content around the fiber rovings is too high for an optimal fiber/matrix stress transfer. Distances between single filaments are in some cases inexistent, as shown in the lower images of Figure 6. Table 4. Fiber volume content estimated from density measurement and rule of mixtures.

Mechanical Characterization
The values of bending strength and Young's modulus of SPS consolidated MMC samples for optimal densification parameters are given in Figure 7. For comparison purposes, the mechanical properties of MMC samples from identical prepregs consolidated by thixoforging process with hydraulic press are shown in Figure 8. Although raw materials and prepreg manufacturing process were the same in both cases, the differences of mechanical properties for both groups of samples are remarkable. SPS consolidated samples exhibit much higher stiffness and lower bending strength in comparison with MMC samples manufactured by alternative consolidation methods. high level of fiber/matrix adhesion could be induced by an uncontrolled growth of interfacial reaction products. Actually, suspicious crystals were found at the fiber surfaces by SEM fractographic analysis of some SPS consolidated MMC samples, as shown for the case of a Cf/AlSi7 sample in the central and right images of Figure 9.    Mechanical properties of SPS consolidated C f /Al samples for optimum densification parameters.

Raman Spectroscopy
Ceramics 2020, 3, 24 272 high level of fiber/matrix adhesion could be induced by an uncontrolled growth of interfacial reaction products. Actually, suspicious crystals were found at the fiber surfaces by SEM fractographic analysis of some SPS consolidated MMC samples, as shown for the case of a Cf/AlSi7 sample in the central and right images of Figure 9.    It is noticeable that, in the case of samples consolidated by SPS, differences of bending strength between each material system are minor. All bending strength values of these samples are higher than 150 MPa and lower than 165 MPa. The reason for his behavior is presumably, that failure mechanisms of SPS consolidated samples are strongly dominated by the elevated interfacial bonding strength. As observed in the failure surface (Figure 9, left image), SPS samples show a brittle behavior without signs of crack deflection, pull-out morphology or fiber debonding. This fact indicates a strong fiber/matrix adhesion, which would be the limiting factor of the composite under flexural stress. This high level of fiber/matrix adhesion could be induced by an uncontrolled growth of interfacial reaction products. Actually, suspicious crystals were found at the fiber surfaces by SEM fractographic analysis of some SPS consolidated MMC samples, as shown for the case of a C f /AlSi7 sample in the central and right images of Figure 9.

Raman Spectroscopy
This presumed carbide formation on the fiber surface was proven by a Raman spectroscopy measurement. The company TTI GmbH-AViSpectro TGU (Stuttgart, Germany) was commissioned for this purpose. According to the results, aluminum carbide is embedded in the surface of carbon fibers in the form of small crystals. The results of the Raman spectroscopy as well as the microscopic image at one of the points where Al 4 C 3 was found are shown in Figure 10.
Ceramics 2020, 3, 24 273 This presumed carbide formation on the fiber surface was proven by a Raman spectroscopy measurement. The company TTI GmbH-AViSpectro TGU (Stuttgart, Germany) was commissioned for this purpose. According to the results, aluminum carbide is embedded in the surface of carbon fibers in the form of small crystals. The results of the Raman spectroscopy as well as the microscopic image at one of the points where Al4C3 was found are shown in Figure 10.

Discussion
The main point to analyze in this chapter is the reason for the notable differences between failure mechanisms and mechanical properties of MMC samples consolidated by SPS and by hydraulic pressing. Considering the morphology of failure surfaces, SPS consolidated samples show no signs of energy dissipation phenomena at the interface. Indeed, aluminum carbide formation at the interface was detected by Raman Spectroscopy only in SPS consolidated samples. These differences of interface properties between both kinds of samples are caused by the different consolidation techniques, as raw materials and prepreg manufacturing parameters were the same for all the samples.
Some recent studies about SPS densification of short carbon fibers and aluminum particles have reported how SPS processing with certain pulse conditions leads to uncontrolled growth of reaction zones at the interface [18]. According to some publications, decreases of the ON:OFF ratio elevates the momentary current intensity, which can increase local processing temperatures due to Joule heating [23,24]. According to Lalet et al., liquid phase was observed at a low ON:OFF ratio, although having set the processing temperature to 500 °C. This indicates a local temperature increase above the melting point of aluminum (660 °C) during SPS densification of short fiber reinforced aluminum [18]. Following the argumentation of the authors, the Al2O3 passivation layer of the Al particles, which were used as raw materials in the mentioned study, might be broken by internal stresses derived from melting-expansion iterations during SPS heating process. An analogy between

Discussion
The main point to analyze in this chapter is the reason for the notable differences between failure mechanisms and mechanical properties of MMC samples consolidated by SPS and by hydraulic pressing. Considering the morphology of failure surfaces, SPS consolidated samples show no signs of energy dissipation phenomena at the interface. Indeed, aluminum carbide formation at the interface was detected by Raman Spectroscopy only in SPS consolidated samples. These differences of interface properties between both kinds of samples are caused by the different consolidation techniques, as raw materials and prepreg manufacturing parameters were the same for all the samples.
Some recent studies about SPS densification of short carbon fibers and aluminum particles have reported how SPS processing with certain pulse conditions leads to uncontrolled growth of reaction zones at the interface [18]. According to some publications, decreases of the ON:OFF ratio elevates the momentary current intensity, which can increase local processing temperatures due to Joule heating [23,24]. According to Lalet et al., liquid phase was observed at a low ON:OFF ratio, although having set the processing temperature to 500 • C. This indicates a local temperature increase above the melting point of aluminum (660 • C) during SPS densification of short fiber reinforced aluminum [18]. Following the argumentation of the authors, the Al 2 O 3 passivation layer of the Al particles, which were used as raw materials in the mentioned study, might be broken by internal stresses derived from melting-expansion iterations during SPS heating process. An analogy between passivation layers of Al particles of mentioned study and thermal sprayed Al layers of the present study could explain observed results. Although heated below the liquidus temperature, there could be local temperature increases during the SPS process, thus promoting the formation of Al 4 C 3 .
Regarding the brittle failure mechanisms of SPS consolidated samples, another argument could explain this behavior. The constraint of metallic layers surrounded by reinforcing ceramic phases has been identified in a previous study as a negative-impact factor for toughness of metal matrix composites [25]. Suboptimal filament distribution in the MMC samples of this study, with fibers stacking together in large areas, may impair toughness of the whole composite. An increase of aluminum thickness between filaments would lead to a toughness enhancement.

Conclusions
The suitability of SPS technique for production of continuous carbon fiber reinforced aluminum was analyzed and proven for the first time in this work. MMC samples were consolidated with remarkable infiltration results. The stable process management of modern SPS equipment enables an accurate control of main densification parameters: temperature and pressure. This parameter accuracy is required to optimize the shear thinning rheological behavior of aluminum alloys at semi-solid temperatures.
According to the mechanical characterization of the samples, stiffness values in the order of 115-135 GPa were achieved. Considering the low density of this material system, values of specific stiffness double those of standard Al-alloys, like EN AW 6082. However, SPS consolidated composites exhibited reduced damage tolerance and suboptimal interface properties. This aspect should be improved in future studies.