Effects of melt temperature and hold pressure on the tensile and fatigue properties of an injection molded talcfilled polypropylene.
INTRODUCTION
Mineralfilled polypropylene has many potential applications in automobiles, appliances, and other commercial products where creep resistance, stiffness, and some toughness are demanded in addition to weight and cost savings. The mechanical behavior of mineralfilled polypropylene and short glass or carbon fiberreinforced polypropylene has been the subject of many studies over the last few years [15]. Limited research has also been done to examine the relationship between their tensile properties, microstructure, and processing conditions [615]. A few of these studies have focused on talcfilled polypropylene. For example, Dave and Chundury [12] used a "design of experiment" approach to determine the effects of several injection molding conditions on the tensile strength of talcfilled polypropylene. They observed that tensile strength increased with both barrel temperature as well as mold temperature. GuerricaEchevaria et al. [13] found that modulus and yield strength of 10%, 20%, and 40% talcfilled polypropylenes were affected slightly with increasing mold temperature as well as increasing melt temperature, but injection rate and screw rotation speed did not have much effect on these two properties. However, screw rotation speed had a very severe effect on the ductility of talcfilled polypropylenes. DiezGutierrez et al. [14, 15] studied the heterogeneity and anisotropy of injectionmolded talcfilled polypropylene discs using dynamic mechanical analysis and thermomechanical analysis. They reported a high degree of anisotropy in these discs due to preferred orientation of talc particles in the flow direction. In this article we report the effects of two injection molding parameters, namely, melt temperature and hold pressure, on the tensile and stresscontrolled fatigue properties of a 40 wt% talcfilled polypropylene. In an earlier article [16], we reported the effects of specimen orientation, stress concentration, weld lines, and frequency on the stresscontrolled fatigue properties of the same material. To our knowledge, the effect of injection molding parameters on the fatigue behavior of talcfilled polypropylene has not been studied in the past. EXPERIMENTAL The material investigated in this study was a 40 wt% talcfilled polypropylene homopolymer available from Ferro (Cleveland, OH) under the grade name TP40AC52BK. The average flow rate of this material, as reported by Ferro, was 6.8 g / 10 min (measured under ASTM D1238 condition). The melting point of the polypropylene matrix was 160[degrees]C. Square plates, 150 X 150 mm, were injectionmolded from the pellets in a single edgegated mold with a central 25mm diameter core (Fig. 1). The plate thickness was 2.5 mm. A 90ton Toyo injection molding machine was used to mold these plates. Three different melt temperatures were considered: 209, 232, and 277[degrees]C. The peak injection pressure was 103 MPa for all plates, but the hold pressure was varied at three levels: 27.6, 55.2, and 82.7 MPa. The mold temperature was maintained at 35[degrees]C. The following two groups of plates were injection molded: [FIGURE 1 OMITTED] (1) Group I: Hold pressure = 55.2 MPa and melt temperature = 209, 232, and 277[degrees]C (2) Group II: Melt temperature = 232[degrees]C and hold pressure = 27.6, 55.2, and 82.7 MPa Dogboneshaped specimens were prepared from the injectionmolded plates in three different directions: parallel to the flow direction (Ldirection specimens), normal to the flow direction (Wdirection specimens), and with weld line (WL specimens). The specimen dimensions were 100 mm in overall length, 25 mm in gage length, and 12.7 mm in gage width. For the WL specimens, the weld line was located at the midlength. The weld line was formed in the plates as the flow front was divided by the central core in the mold and then joined behind the core. Uniaxial tensile tests and fatigue tests were performed on an MTS servohydraulic testing machine. The tensile tests were conducted at 1.25 mm/min, which was approximately equivalent to a strain rate of 0.05 [min.sup.1]. Three tensile parameters were determined from each stressstrain curve: elastic modulus (E) from the initial slope, yield strength ([[sigma].sub.y]) corresponding to the maximum stress observed, and yield strain ([[epsilon].sub.y]) corresponding to the yield strength. Stresscontrolled cyclic fatigue tests were performed in tensiontension mode at an ambient temperature of ~23[degrees]C. The ratio of the minimum cyclic stress to the maximum cyclic stress (i.e., Rratio) was 0.1. The cyclic frequency was 1 Hz. Such a low frequency was selected so that fatigue failure would occur instead of thermal failure [16]. [FIGURE 2 OMITTED] RESULTS Tensile Properties Figure 2 shows the tensile stressstrain curves of the 40 wt% talcfilled polypropylene specimens parallel to the flow direction (L), normal to the flow direction (W), and with weld line (WL) under the different processing conditions considered. It can be observed in these figures that the stressstrain relationships were nonlinear even at strains lower than the yield strain. Each curve shows a maximum stress, which was assumed to be the yield strength of the material. After reaching the maximum stress, the specimen with the weld line failed almost immediately; however, for the Ldirection and Wdirection specimens, stress decreased steadily with strain until fracture occurred. The mean value and the standard deviation of the tensile properties obtained from three specimens for different processing conditions are listed in Table 1. The yield strength in the Ldirection was higher than that in the Wdirection. The difference in properties in these two mutually perpendicular directions indicates inherent anisotropy of the injectionmolded talcfilled polypropylene plates. The presence of weld line in WL specimens significantly decreased the yield strength and failure strain. However, the weld line did not influence the modulus. Figure 2a shows the effect of melt temperature on the tensile behavior of the talcfilled polypropylene. The hold pressure for these specimens was 55.2 MPa. For specimens parallel to the flow direction, the yield strengths at different melt temperatures were very close and the stressstrain curves after yielding did not show much difference. For specimens normal to the flow direction, the yield strength and stress level after yielding were significantly lower at melt temperature 277[degrees]C. The tensile orientation factor, defined as the ratio of yield strengths of the Ldirection and the Wdirection specimens, changed from 1.05 at melt temperature 209[degrees]C to 1.27 at melt temperature 277[degrees]C. For specimens with weld line, yield strength increased with increasing melt temperature. The tensile weld line factor, defined as the ratio of the yield strengths of the Ldirection specimens and the WL specimens, was 1.55 at melt temperature 209[degrees]C and decreased to 1.43 at melt temperature 277[degrees]C. [FIGURE 3 OMITTED] [FIGURE 4 OMITTED] Figure 2b shows the effect of hold pressure on the tensile behavior of the talcfilled polypropylene. The melt temperature for these specimens was 232[degrees]C. Increasing the hold pressure increased the yield strengths for all three types of specimens. But the anisotropy of the talcfilled polypropylene was not very sensitive to hold pressure. The tensile orientation factors were 1.06, 1.06, and 1.07 at hold pressure 27.6 MPa, 55.2 MPa, and 82.7 MPa, respectively. However, the weldline strength increased with increasing hold pressure. The tensile weld line factor dropped from 1.56 at hold pressure 27.6 MPa to 1.31 at hold pressure 82.7 MPa. [FIGURE 5 OMITTED] [FIGURE 6 OMITTED] [FIGURE 7 OMITTED] Figure 3 shows that both tensile modulus and yield strength of the talcfilled polypropylene varied linearly with melt temperature and hold pressure. The linear relationships observed in these plots are modeled with the following equations: [[sigma].sub.Y] = [[sigma].sub.Y0][1 + [J.sub.melt](T  [T.sub.0])][1 + [J.sub.pressure](P  [P.sub.0])] (1) E = [E.sub.0][1 + [L.sub.melt](T  [T.sub.0])][1 + [L.sub.pressure](P  [P.sub.0])] (2) where [J.sub.melt], [L.sub.melt] and [J.sub.pressure], [L.sub.pressure] are melt temperature sensitivity factors and hold pressure sensitivity factors, [T.sub.0] and [P.sub.0] are the reference melt temperature and reference mold pressure, and [[sigma].sub.Y0] and [E.sub.0] are the reference yield strength and modulus. The average values of [J.sub.melt], [L.sub.melt], [J.sub.pressure], and [L.sub.pressure] are listed in Table 2. Fatigue Properties Figure 4 shows the SN curves of the 40 wt% talcfilled polypropylene parallel to the flow direction (L), normal to the flow direction (W), and with weld line (WL) at different melt temperatures. The hold pressure for these specimens was 55.2 MPa. The fatigue strength in Ldirection was much higher than that in the Wdirection. The presence of weld line decreased the fatigue strength even further. Similar to the tensile test results, melt temperature did not have any effect on the fatigue strength of the Ldirection specimens. However, for the Wdirection specimens fatigue strength decreased with increasing melt temperature and for the WL specimens, fatigue strength increased with increasing melt temperature. [FIGURE 8 OMITTED] Figure 4 also shows the effect of hold pressure on the fatigue behavior of the talcfilled polypropylene. The melt temperature in this case was 232[degrees]C. As before, the Ldirection specimens had the highest fatigue strength and the WL specimens had the lowest fatigue strength. The fatigue strength for all three types of specimens increased with increasing hold pressure. The highest increase occurred when the hold pressure was increased from 55.2 to 82.7 MPa. Based on the experimental results, the following empirical equation, similar to the Basquin equation used for stresslife data of metals [17], was fitted to the SN curves corresponding to each processing condition: [sigma] = [[sigma].sub.f]([N.sub.f])[.sup.b] (3) where, [sigma] = fatigue stress level, [N.sub.f] = number of cycle to failure at [sigma], [[sigma].sub.f] = fatigue strength coefficient, b = fatigue strength exponent. The values of fatigue strength coefficient [[sigma].sub.f] and fatigue strength exponent b at different processing conditions are listed in Table 1 and are plotted in Figs. 5 and 6 as a function of melt temperature and hold pressure, respectively. Figure 5 shows that [[sigma].sub.f] for the Ldirection specimens and WL specimens increased with increasing melt temperature, while [[sigma].sub.f] for the Wdirection specimens decreased with increasing melt temperature. Figure 5 also shows that the variation of fatigue strength exponent b with melt temperature was very small, and therefore, in the melt temperature range considered, b was assumed to be a constant. Figure 6 shows the variation of fatigue strength coefficient [[sigma].sub.f] and fatigue strength exponent b with hold pressure. The values of [[sigma].sub.f] for all three types of specimens increased with increasing hold pressure; however, the fatigue strength exponent b was not much affected by hold pressure. Thus, in the range of hold pressures considered, b was assumed to be a constant. The following empirical relationship was found to fit the combined effect of melt temperature and hold pressure on [[sigma].sub.f]: [FIGURE 9 OMITTED] [[sigma].sub.f] = [[sigma].sub.f0][1 + [K.sub.melt](T  [T.sub.0])][1 + [K.sub.pressure](P  [P.sub.0])] (4) where [K.sub.melt] and [K.sub.pressure] are melt temperature sensitivity factor and hold pressure sensitivity factor in fatigue, [T.sub.0] and [P.sub.0] are reference melt temperature and reference mold pressure, and [[sigma].sub.f0] is the reference fatigue strength coefficient. The average values of [K.sub.melt], [K.sub.pressure] and b of the talcfilled polypropylene are listed in Table 2. The value of [K.sub.melt] with weld line was much higher than that in the flow direction and the [K.sub.melt] normal to the flow direction was negative. The values of [K.sub.pressure] in the flow direction and normal to the flow direction were close, but [K.sub.pressure] with weld line was higher than that in the flow direction and normal to the flow direction. Fracture Surface Observations The fracture surfaces of several fatigue specimens were examined under scanning electron microscope to determine the differences in the Ldirection, Wdirection, and WL specimens. Each fracture surface exhibited skincore morphology with different degrees of talc particle orientations in the core and in the skin. The relative size of the core and the skin varied with processing condition. In general, the greater the talc particle orientation parallel to the loading direction, the higher will be strength, since they are more effective in stress transfer than those oriented normal to the loading direction. The processing condition also affects the molecular orientation and crystalline morphology in the skins and core of injectionmolded polypropylene; however, their effects on mechanical properties may be of less importance than the effect of filler orientation in a highly filled polypropylene [6]. [FIGURE 10 OMITTED] Figure 7 shows the fracture surfaces of the Ldirection specimens at different processing conditions. On each fracture surface, there was evidence of skincore morphology, with the skins containing many talc particles oriented normal to the loading direction. Talc particles in the core were oriented parallel to the loading direction, which was also the flow direction for the specimens. The parabolic flow pattern in the core was also clearly visible in Figure 7. The skins were relatively thin compared to the core and their thickness did not change much with melt temperature. However, the skin thickness decreased with increasing hold pressure. Skincore morphology was also found on the fatigue fracture surfaces of the specimens normal to the flow direction (Fig. 8). In this case, many talc particles in the core were oriented normal to the loading direction (Fig. 9). With increasing hold pressure, the talc particle orientation normal to the loading direction was reduced, which explains the increase in yield strength and fatigue strength of these specimens at higher hold pressure. Figure 10 shows the fracture surfaces of WL specimens containing a weld line. In these specimens, the skincore morphology was very clearly visible. The white band in the core contained talc particles that were oriented normal to the loading direction. The darker zones in the skins contained talc particles oriented parallel to the loading direction. The thickness of the core decreased and the thickness of the skins increased with increasing melt temperature and increasing hold pressure (Table 3). This explains the reason for increasing yield strength and fatigue strength with either increasing melt temperature or increasing hold pressure. CONCLUSIONS Static tensile and fatigue tests were performed on 40 wt% talcfilled polypropylene injection molded at three different melt temperatures and three different hold pressures. It was observed that yield strength and fatigue strength of the talcfilled polypropylene specimens were lower normal to the flow direction than in the flow direction, indicating inherent anisotropy in the material. Yield strength and fatigue strength of the talcfilled polypropylene with weld line were significantly lower than those without weld line. Yield strength and fatigue strength of the talcfilled polypropylene in the flow direction was not influenced by melt temperature, but they increased with increasing hold pressure. Yield strength and fatigue strength of the talcfilled polypropylene normal to the flow direction decreased with increasing melt temperature, but they increased with increasing hold pressure. Yield strength and fatigue strength of the talcfilled polypropylene with weld line increased with increasing melt temperature as well as increasing hold pressure. Both melt temperature and hold pressure influenced skincore morphology exhibiting different orientations of talc particles in the skins than in the core. TABLE 1. Tensile and fatigue properties of 40w% talcfilled polypropylene at different processing conditions. Melt temp. Hold pressure Tensile modulus ([degrees]C) (MPa) Direction (GPa) 209 55.2 L 8.48 [+ or ] 0.24 209 W 7.92 [+ or ] 0.32 209 WL 6.56 [+ or ] 0.32 232 55.2 L 8.62 [+ or ] 0.13 232 W 7.51 [+ or ] 0.25 232 WL 6.48 [+ or ] 0.43 277 55.2 L 8.82 [+ or ] 0.27 277 W 7.41 [+ or ] 0.36 277 WL 6.94 [+ or ] 0.48 232 27.6 L 8.82 [+ or ] 0.25 232 W 7.22 [+ or ] 0.36 232 WL 6.71 [+ or ] 0.39 232 82.7 L 9.61 [+ or ] 0.32 232 W 8.13 [+ or ] 0.30 232 WL 6.92 [+ or ] 0.26 Melt temp. Yield strength Failure strain ([degrees]C) (MPa) (%) 209 27.03 [+ or ] 0.16 2.96 [+ or ] 0.12 209 25.70 [+ or ] 0.23 2.39 [+ or ] 0.22 209 17.49 [+ or ] 0.13 0.79 [+ or ] 0.10 232 27.21 [+ or ] 0.12 2.80 [+ or ] 0.23 232 25.39 [+ or ] 0.26 2.57 [+ or ] 0.14 232 17.88 [+ or ] 0.22 0.91 [+ or ] 0.02 277 27.38 [+ or ] 0.08 3.25 [+ or ] 0.17 277 22.57 [+ or ] 0.16 1.87 [+ or ] 0.12 277 19.11 [+ or ] 0.21 1.00 [+ or ] 0.03 232 26.61 [+ or ] 0.02 3.08 [+ or ] 0.11 232 25.15 [+ or ] 0.37 2.69 [+ or ] 0.12 232 17.06 [+ or ] 0.24 0.86 [+ or ] 0.03 232 29.52 [+ or ] 0.19 2.95 [+ or ] 0.10 232 27.62 [+ or ] 0.26 2.67 [+ or ] 0.06 232 22.47 [+ or ] 0.32 1.31 [+ or ] 0.03 Melt temp. ([degrees]C) [[sigma].sub.f] (MPa) b 209 32.18 0.0306 209 28.49 0.0283 209 18.23 0.0202 232 32.19 0.0312 232 26.28 0.0236 232 19.82 0.0216 277 32.58 0.0303 277 26.04 0.0277 277 20.73 0.0210 232 31.38 0.0304 232 25.23 0.0264 232 18.91 0.0263 232 34.91 0.0299 232 29.35 0.0252 232 24.95 0.0247 TABLE 2. Processing condition factors of 40w% talcfilled polypropylene. Property Parameter In the flow (L) direction Yield strength [J.sub.melt] 0.0050 [J.sub.pressure] 0.53 [L.sub.melt] 0.0049 [L.sub.pressure] 0.20 Fatigue strength [K.sub.melt] 0.011 [K.sub.pressure] 0.64 b 0.031 Property Parameter Normal to the With weld line flow (W) direction Yield strength [J.sub.melt] 0.048 0.024 [J.sub.pressure] 0.45 0.98 [L.sub.melt] 0.0068 0.0062 [L.sub.pressure] 0.17 0.038 Fatigue strength [K.sub.melt] 0.032 0.034 [K.sub.pressure] 0.75 1.10 b 0.027 0.023 TABLE 3. Effect of melt temperature and hold pressure on the core and skin thickness values in the weldline specimens. Melt temp. Hold pressure Approx. core Approx. total skin ([degrees]C) (MPa) thickness (mm) thickness (mm) 209 55.2 1.40 1.10 232 55.2 1.35 1.15 277 55.2 1.17 1.33 232 27.6 1.45 1.05 232 55.2 1.35 1.15 232 82.7 0.97 1.53 Contract grant sponsors: Ford Motor Company, TRW Education Foundation. REFERENCES 1. J.P. Trotignon, L. Demdoum, and J. Verdu, Composites, 23, 313 (1992). 2. J.P. Trotignon, L. Demdoum, and J. Verdu, Composites, 23, 319 (1992). 3. S.Y. Fu, B. Lauke, E. Mader, C.Y. Yue, and X. Hu, Composites, Part A, 31, 1117 (2000). 4. J.L. Thomason, M.A. Vlug, G. Schipper, and H.G.L.T. Krikor, Composites, Part A, 27A, 1075 (1996). 5. J.L. Thomason and M.A. Vlug, Composites, Part A, 28A, 277 (1997). 6. M. Fujiyama, H. Awaya, and S. Kimura, J. Appl. Polym. Sci., 21, 3291 (1977). 7. G. Kalay and M. J. Bevis, J. Polym. Sci.: Part B: Polym. Phys., 35, 241 (1997). 8. R. Mendoza, G. Regnier, W. Seiler, and J.L. Lebrun, Polymer, 44, 3363 (2003). 9. G. Kalay and M. J. Bevis, J. Polym. Sci.: Part B: Polym. Phys., 35, 265 (1997). 10. M. Akay and D. Barkley, J. Matl. Sci., 26, 2731 (1991). 11. J.P. Tancrez, J. Pabiot, and F. Rietsch, Comp. Sci. and Tech., 56, 725 (1996). 12. P. Dave and D. Chundury, J. Inj. Molding Tech., 1, 181 (1997). 13. G. GuerricaEchevaria, J.I. Eguiazabal, and J. Nazabal, Eur. Polym. J., 34, 1213 (1998). 14. S. DiezGutierrez, M.A. RodriguezPerez, J.A. De Saja, and J.I. Velasco, Polymer, 40, 5345 (1999). 15. S. DiezGutierrez, M.A. RodriguezPerez, J.A. De Saja, and J.I. Velasco, J. Appl. Polym. Sci., 77, 1275 (2000). 16. Y. Zhou and P.K. Mallick, Polym. Eng. Sci., 45, 510 (2004). 17. J.A. Bannantine, J.J. Comer, and J.L. Handrock, Fundamentals of Metal Fatigue Analysis, Prentice Hall, New York (1990). Yuanxin Zhou, P.K. Mallick Center for Lightweighting Automotive Materials and Processing, University of MichiganDearborn, Dearborn, Michigan 48128 Correspondence to: P.K. Mallick; email: pkm@umich.edu 

Reader Opinion