optimization of powder injection molding of feedstock based on aluminum oxide and multicomponent...
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Optimization of Powder Injection Molding ofFeedstock Based on Aluminum Oxide andMulticomponent Water-Soluble Polymer Binder
Berenika Hausnerova,1 Lucie Marcanikova,1 Petr Filip,2 Petr Saha11 Polymer Centre, Faculty of Technology, Tomas Bata University in Zlın, TGM 275, 762 72 Zlın, Czech Republic
2 Department of Mechanics of Fluids and Disperse Systems, The Institute of Hydrodynamics, Academy ofSciences of the Czech Republic, Pod Patankou 5, 166 12 Prague, Czech Republic
Analyses crucial to optimize powder injection moldingof feedstock based on aluminum oxide powder andmulticomponent polymeric binder are provided withthe aim to obtain defect-free, high density parts. Asthe critical step of the process is the flow of highlyfilled (60 vol%) compound into a mold cavity, rheologi-cal properties supplemented by thermal and pressure-volume-temperature characteristics are measured anddescribed. Upon shear deformation the feedstockundergoes structural changes, which are quantified interms of yield stresses obtained using Herschel-Bulk-ley and Casson methods. Further, the rheologicalmodel is developed to describe the flow behavior ofthe feedstock in the whole shear rate range measured.Thermogravimetric analysis is performed to optimizedebinding step of the process, and two possible waysof the binder removal are proposed: purely thermaland combined solvent/thermal. The quality of the finalsintered parts is demonstrated on scanning electronmicroscopic images of their surfaces. POLYM. ENG.SCI., 51:1376–1382, 2011. ª 2011 Society of Plastics Engineers
INTRODUCTION
Powder injection molding (PIM) is an effective (high
added value) and attractive alternative to the traditional
processes (machining, investment casting) for the produc-
tion of complex-shaped small parts. It combines a com-
mon processing route for plastics—injection molding—
with metallurgical sintering.
PIM process might be generally divided into four con-
sequential steps: (1) compounding metal or ceramic pow-
der with a polymers mixture (called ‘‘binder’’) to obtain
homogeneous highly filled feedstock, (2) injection mold-
ing of prepared feedstock into a mold with a required
design resulting in a ‘‘green’’ part, (3) thermal and/or sol-
vent removal of a polymer binder creating a ‘‘brown’’
part, and (4) sintering the remaining powder structure to a
high density component [1].
The process phase that still requires clarification and
optimization is the flow of highly filled feedstock into a
mold cavity during injection molding since the defects in
the final parts (after sintering) are created during molding
and cannot be reduced or eliminated during the following
steps as debinding and sintering [2].
Thus, investigation of flow properties is of crucial im-
portance in the PIM process optimization. While the rhe-
ology of suspensions of noninteracting spheres seems to
be well established, the understanding rheological
behavior of multiphase systems as those intended for PIM
represents a difficult task. For the cavity filling with mini-
mized jetting a pseudoplastic flow that relieves process-
ability is required [1]. Although, it is a common cause for
unfilled polymers, PIM compounds show a complicated
sensitivity to variations with shear rate, even if the binder
behaves in a Newtonian fashion. Upon powder loading,
the Newtonian plateau becomes reduced or disappears. It
has been widely accepted that the change into non-Newto-
nian behavior arises from the disruption of agglomerates
formed by particles [3]. The two mechanisms affecting
viscosity can be discerned: the agglomerates’ destruction
during shearing causes a decrease in the amount of sus-
pending fluid trapped among particles, and thus viscosity
decreases due to the drop of an effective volume fraction
of powder [4], and simultaneously the change in viscosity
is related to the dissipation energy rising from the rotation
and distortion of particle agglomerates (e.g., as shown in
Ref. 5).
A yield point often appears at low shear rates as an in-
dication of temporary particle network structure within
Correspondence to: Berenika Hausnerova; e-mail: [email protected]
Contract grant sponsor: The Grant Agency of the Czech Republic; contract
grant number: 103/08/1307; contract grant sponsor: The Ministry of Educa-
tion, Youth and Sports of the Czech Republic; contract grant number:
MSM 7088352101.
DOI 10.1002/pen.21928
Published online in Wiley Online Library (wileyonlinelibrary.com).
VVC 2011 Society of Plastics Engineers
POLYMER ENGINEERING AND SCIENCE—-2011
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melt (e.g., [6, 7]), although some authors claim that yield
stress might be a result of extrapolation rather than a real
phenomenon [8, 9] as pointed out by Kurzbeck et al. [3].
However, from the engineering viewpoint, the Casson
method [5] based on an energy dissipation mechanism or
the empirical Herschel-Bulkley model [10] are widely
accepted ways of yield stresses evaluation.
Upon further increase of shear rates the particle struc-
ture is destroyed, particles and polymer orientate and
order in the flow direction to allow interparticle motion,
and the viscosity is dominated by hydrodynamic interac-
tions [11] resulting in shear thinning.
Highly concentrated compounds (about 50 vol% solids
and higher) may exhibit a radical change on their flow
curves accompanied by distortions of the extrudate sur-
face expressing themselves similarly to the spurt flow of
e.g., linear polyethylene [12, 13]. The mechanism of these
flow instabilities is however different as investigated and
reported in [14–16].
Because PIM is a high-pressure molding process, flow
behavior, and compressibility of the powder and polymer-
based binder in a pressurized melt-stage are key indicators
for the assessment of processing conditions. The pressure-
volume-temperature (PVT) characteristic provides infor-
mation about the specific volume of feedstock at the
molding temperature and the pressure necessary for the
production of defect-free, injection molded parts.
Although the shrinkage of a green body is needed to be
incorporated into the mold design, PVT studies on PIM
materials are reported scarcely [17–20]. Further, Greene
and Heaney [19] proved that the holding pressure could
be effectively used to control the dimensional stability of
the final sintered parts. An excessive pressure may cause
relaxation problems and higher shrinkage as reported also
by Laddha et al., [17] for aluminum oxide (56 vol%)
feedstock. This results in a suggestion of choosing the
holding pressure level after appropriately referring to
PVT-diagram in such a way that the residual pressure in a
cavity before mold opening is near to the atmospheric
one.
In this article, the PIM process of aluminum oxide
(alumina) feedstocks is optimized. Although metals such
as stainless steels (316L, 17-4PH) are nowadays prevail-
ing PIM material, aluminum oxide parts (thread guides)
represent the earliest PIM application dating back to the
1930s [21]. The advantage of alumina powder as the most
widely used PIM ceramic [22] over the metals consists in
a combination of good mechanical properties with a low
specific weight. The PIM alumina products find their
application in areas where are exposed to extreme condi-
tions such as high temperatures, corrosive atmosphere, ab-
rasive conditions, or high loads at extreme temperatures
[23]. Due to the above properties, alumina powder is uti-
lized in chemical and electronic industries as chemical
processing and heat treatment equipments, melting cruci-
bles and inject printheads, and an increasing potential of
ceramics is registered also in a medical sector as cardiac
rhythm management, cardiovascular and endoscopic devi-
ces, neurological sensors and stimulators, cochlear
implants, dental implants and abutments, fluid handling,
and small joints.
The aim is to produce nondefect parts via careful con-
trol of the flow properties of the feedstock. As already
pointed out, the problems created during flow into a mold
appear during/after debinding and/or sintering, and there-
fore, their solution consists in rheology. In addition, ther-
mogravimetric analysis (TGA) to set the conditions for
debinding is provided. In the recent years, solvent debind-
ing combined with a thermal method becomes common
as decreases a cycle time. Organic solvents predominantly
used (n-heptane, acetone, trichlorethane) are flammable,
carcinogenic and environmental pollutants [24]. Thus,
the water-soluble binder components (polyethylene
glycol, polyvinyl alcohol, agar, etc.) appear as favorable
alternative.
EXPERIMENTAL
Materials
In this study, highly compressive superground alumi-
num oxide (alumina) powder MARTOXID1 MR70
(Albemarle Corporation) with a specific surface area
(BET) 6–10 m2/g, bulk density � 0.90 g/cm3, green den-
sity 2.20-2.40 g/cm3, and fired density (1,6008C, 2 h)
3.80-3.92 g/cm3 was used, see Fig. 1. The particle size
distribution was measured using ANALYSETTE 22
MicroTec plus (FRITSCH GmbH, Germany) equipment,
and Table 1 compares the obtained data with the data
sheet determined with CILAS 1064 (CILAS, France).
The powder was compounded with a commercial
multicomponent binder Licomont EK 583-G (Clariant,
Switzerland), which is partially water-soluble with a den-
sity 1.05-1.15 g/cm3 and the softening point at 105-
1158C. During mixing in a blade kneader at 1608C for
2 h a surfactant (1 wt% oleic acid) was added. Subse-
quently, 60 vol% feedstock in a form of pellets was
acquired from a single-screw extruder.
Methods
Rheological properties of the alumina feedstock were
measured using a capillary rheometer Rheograph 2001
(Gottfert, Germany) at shear rates from 101 to 104 sec21
at temperatures 150, 160, and 1708C. The length-to-diam-
eter (L/D) ratio of capillary was 30. The apparent viscos-
ity values are presented since the data measured with an
orifice capillary (L/D ¼ 0.12/1) were rather scattered.
Rheological behavior of the binder was determined with
the help of a rotational rheometer Physica MCR501
(Anton Paar, Austria). Shear viscosities were measured at
shear rates ranging from 1021 to 6 3�102 sec21 and at
temperatures from 150 to 1708C in steps of 58C.
DOI 10.1002/pen POLYMER ENGINEERING AND SCIENCE—-2011 1377
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PVT characteristics were obtained with a PVT-100
(SWO, Germany) apparatus. The specific volumes were
examined at pressures and temperatures in the range 30–
200 MPa and 50-2508C, respectively, in a measurement
mode of isobaric heating with a heating rate of 58C/min.
Thermal properties were determined via a differential
scanning calorimeter (DSC) Pyris 1 DSC (Perkin-Elmer)
in a sealed aluminum pans under nitrogen atmosphere
with heating/cooling rate 108C/min at temperatures rang-
ing from 45 to 1808C.The TGA was performed with the samples of dimen-
sions (3 3 3 3 2) mm with a SETSYS Evolution
1200TG (Setaram, France) thermogravimeter from ambi-
ent temperature to 1,2008C.The green and brown parts’ surface morphologies as
well as the surface of the sintered parts were observed
with a scanning electron microscopy (SEM) using Vega II
(Tescan, Czech Republic) microscope operated at 10 kV;
all samples were coated with a thin layer of gold using a
polaron sputtering apparatus.
RESULTS AND DISCUSSION
From Fourier Transform Infrared Spectroscopy analysis
(not included) it is supposed that the binder contains poly-
olefines, paraffin waxes, and polyethyleneglycols. Its
rheological characteristic was acquired at five different
temperatures in the range 150-1708C in steps of 58Cusing the rotational rheometer. The effect of temperature,
especially at shear rates higher than 10 sec21, is not so
pronounced with increasing temperature above 1608C(Fig. 2). Overall level of binder viscosity lies in the range
proposed for PIM technology, that is, \0.1 Pa.s at the
processing shear rate to provide PIM mixtures with vis-
cosity below 1,000 Pa.s [25].
Filling the binder with 60 vol% alumina powder
resulted in the feedstock with flow properties far from
required above. Fine alumina powder is relatively
hydroscopic and binder is rather sensitive to destabili-
zation in water resulting in enhanced viscosity. This
problem can be solved via improving the ‘‘flowability’’
of the system with dispersants and lubricating agents.
Reduction of viscosity about one order of magnitude
has been reported by Lin and German [26] for
56 vol% alumina powder in a paraffin wax added with
4 wt% of stearic acid (SA). In case of Chan and
Lin [27] SA molecules adsorption on alumina powder
surface changed the flow course from dilatant to
pseudoplastic.
The rheological data obtained for 60 vol% alumina
feedstock modified with 1 wt% oleic acid are depicted in
Fig. 3. Oleic acid has been chosen with regard to investi-
gation by Tseng [28] comparing the effect of stearic acid,
TABLE 1. Particle size distribution of alumina powder.
Fraction (%)
Particle Size (lm)
CILAS 1064 ANALYSETTE 22
\10 0.200–0.400 0.240
\50 0.500–0.800 0.643
\90 1.500–3.000 2.573
FIG. 2. Temperature-dependent viscosity versus shear rate of multi-
component binder.
FIG. 3. Temperature-dependent viscosity versus shear rate of alumina
feedstock.
FIG. 1. Scanning electron micrograph of alumina powder.
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oleic acid, and 12-hydroxystearic acid (2 wt%) on the
flow behavior of 60 vol% alumina feedstock. Their meas-
urements at high shear rates region (1,000–15,000 sec21)
showed similar effect of SA and oleic acid on mixture
viscosity at 1508C. In addition Persson et al. [18] demon-
strated that 1% of SA added to the iron-based feedstock
has the same effect as 2% of SA, decreasing viscosity
four times.
The viscosity values (Fig. 3) are about three to two
orders of magnitude higher in comparison to binder viscos-
ity at the corresponding shear rates. At lower shear rates
(up to 500 sec21) the viscosity of feedstock decreases with
increasing shear rate suggesting particle or binder molecule
orientation and ordering with flow. When the shear rate
reaches 500 sec21 particles cannot form layers and slide
over each other as firstly reported by Hoffman [29], and
shear thinning turns into a dilatant flow. Similar phenom-
enon was observed for all investigated temperatures. There
is still considerable uncertainty about the source of such
behaviour. Jansma and Qutubuddin [30], who studied this
phenomenon using different viscometers, showed that it
could not be an experimental artefact due to the wall slip.
The mechanism proposed by Barnes [31] is that with
increasing shear stress (rate) the layers formed in the pseu-
doplastic flow region becomes disrupted, and at a certain
shear stress (rate) are fully eliminated (flow turns into dilat-
ant). It implies that every highly concentrated suspension
exhibits dilatant flow if proper flow conditions (depending
on filler concentration, particle size distribution as well as
viscosity of a polymer component) are selected.
For the alumina feedstock investigated, this structure
restructuralization appears repeatedly what reflects in
repeated changes between pseudoplastic and dilatant flow
behavior. Herschel-Bulkley [10] and Casson [5] models
applied to the rheological data resulted in similar values
of yield stress as can be seen from Table 2, corresponding
well to Kurzbeck et al. [3] studying inorganic pigment/
paraffin wax compounds, supporting Casson’s idea of
energy dissipation mechanism responsible for viscosity
variation with shear rate.
Herschel-Bulkley and Casson models cannot describe the
flow properties of alumina feedstock in the whole range of
the measured data because classical empirical models are
primarily determined for characterization of monotonous de-
pendence of viscosity on shear rate or stress. As the course
of data in Fig. 3 is consecutively shear thinning, shear thick-
ening and again shear thinning, a more complicated model
has to be applied. Among other things it implies a model
with the increased number of empirical parameters. As even
for more complicated shear-thinning (i.e., still monotonous)
materials lacking their ‘‘symmetry’’ (in other words -the
drop-off in viscosity from first Newtonian plateau is mir-
rored by its rapid leveling-off towards second Newtonian
plateau) Roberts et al. [32] used so-called generalized Ellis
model with eight parameters, it is natural that for this non-
monotonous behavior, we apply a model with the same
number of parameters. Further, the model should relate vis-
cosity with shear stress and not shear rate because for two
phase materials the stress is continuous across the interface
whereas the deformation rate is not, see Lomellini and Ferri
[33]. This is exactly the problem with interpretation of rheo-
logical data in Hoffman [29] where he claims that with
increasing volume fraction of suspension the respective
curves viscosity vs. shear rate exhibit discontinuous behav-
ior. If the rheograms are transformed to the relation viscosity
vs. shear stress then there is possible to eliminate the prob-
lem with a seeming discontinuity. For rheological modeling
of the data introduced in Fig. 3 the eight-parameter model
published in Filip et al. [34] is applied
Z ¼ Z1 expð�f1Þb1 þ expðf1Þ þ expð�f1Þ þ
Z2 expð�f2Þb2 þ expðf2Þ þ expð�f2Þ
(1)
where
f1 � f ðg; c1; p1Þ ¼ logðc1tÞp1 ; f2 � f ðg; c2; p2Þ ¼ logðc2tÞp2(2)
TABLE 2. Yield stresses values calculated from Herschel-Bulkley and
Casson models.
Temperature (8C)
Yield Stress (kPa)
Herschel-Bulkley Casson
150 50 47
160 45.5 44
170 40 37
FIG. 4. Temperature-dependent shear stress versus shear rate of alu-
mina feedstock; solid lines represent data fitting by the rheological
model.
TABLE 3. Parameters of rheological model applied to viscosity data
of alumina feedstock.
Parameter (2) [f(T) ¼ 1þ(170 2 T)/80]
a1 108 � f(T) a2 0.02 � f(T)b1 21.9 b2 21.99986
c1 0.034 c2 0.00072
p1 0.635 p2 0.028
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The results of the fitting the experimental data with
this model are shown in Fig. 4 using the relation
s ¼ g � _c, the parameters are summarized in Table 3. The
parameters g1 and g2 represent the values of first and sec-
ond Newtonian plateau, respectively, and they dominantly
influence the maxima of the corresponding peaks. The pa-
rameters bi, ci, and pi significantly participate in the ‘‘geo-
metrical forming’’ of the left (i ¼ 1) and right (i ¼ 2)
peaks. The three parameters consecutively determine the
rate of pseudoplastic/dilatant change, horizontal shift
(along the abscissa), and steepness of the respective peaks
(for more detail see David and Filip [35]). It is necessary
to point out that six out of eight parameters are fixed and
the same for all temperatures, the remaining two depend
on the identical empirically derived temperature-depend-
ent function. It is supposed that the empirical parameters
can be further linked to the materials characteristics when
the corresponding database will be created.
The PVT data of the alumina feedstock under iso-
baric heating regime is shown in Fig. 5. As it can be
seen the temperature transitions are imperceptible. In
contrast, Persson et al. [18] reported (using the same
device) 420 stainless steel feedstock transition zones
corresponding to the particular components of their
commercial binder. Similarly, Wei et al. [20] when
using PVT-100 device for 85 wt% alumina with paraf-
fin wax based binder system obtained the transition
zones indicating clearly the binder components. The
result obtained for alumina feedstock might be
explained as the consequence of the multicomponent
character of the binder whose particular components
have overlapping melting zones as can be seen from the
DSC data (Table 4). Subsequently, DSC data reveals a
slight drop of melting temperature of binder after 60
vol% addition of alumina powder. Specific heat
capacity of the feedstock (cp), determined at three tem-
peratures in the range 120-1608C in 208C steps, varies
with temperature as follows: (1.072 6 0.055), (1.080 60.066), and (1.083 6 0.080) J/(g 8C), respectively.
During debinding process, the binder must be com-
pletely removed before starting the sintering cycle to hold
the shape of the ceramic part. From the debinding meth-
ods, the thermal removal of polymer based binders is
widely used to remove organic components before sinter-
ing. TGA is mostly employed to design a debinding
cycle.
The optimal conditions for debinding and following
sintering of the investigated alumina feedstock are deter-
mined as follows: the heating rate 508C/h from ambient
temperature to 808C, then the heating rate is slowed down
to 108C/h for temperatures in the range 80–2808C, and
finally sintering temperature 1,6008C is reached at the rate
1008C/h. During thermal debinding the binder can leave
the part as liquid or vapor. Liu and Tseng [36] propose
evaporation as a dominant mechanism for the low-molec-
ular-weight binder systems.
Thomas-Vielma et al. [37] investigated for alumina
with HDPE based binder that solvent/thermal combination
decreases the time of a debinding cycle by cca 4 h in
comparison to purely thermal debinding. Figure 6 shows
the weight loss for both thermal and combined solvent/
thermal debinding process. The first stage of major
weight-loss occurs in the temperature range �320–4008C,
FIG. 5. PVT characteristic of alumina feedstock under isobaric regime.
TABLE 4. Melting peak temperatures of polymer binder and alumina
feedstock.
Material
Peak Melting Temperature (8C)
#1 #2 #3 #4
Binder 60.5 6 0.3 77.8 6 0.1 89.2 6 0.1 110.5 6 0.1
Feedstock 58.2 6 0.3 77.0 6 0.3 87.2 6 0.1 109.6 6 0.5
FIG. 6. TGA of binder removal.
FIG. 7. Scanning electron micrographs of final sintered alumina part in
a bulk (a) and detailed (b) resolutions.
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and the second takes place from � 420 to 4708C. The
first stage of binder removal should be closely equivalent
to the removing of binder wax and low-molecular sub-
stances. At this stage the evaporation is assumed to be a
dominant mechanism for the wax removal. Consequently,
the second stage of weight loss is attributed decisively to
the disposal of the low-molecular-weight polyolefines [36]
and polyethyleneglycols. Trunec and Cihlar [38] studied
the influence of various atmospheres for 59.8 vol% alu-
mina filled in EVA based binder. In their case, the atmos-
phere containing oxygen caused defected parts due to the
formation of nonvolatile layer from oxidative degradation
slowing down the evaporation of low-molecular-weight
components. On the opposite, binder removal in nitrogen
and carbon dioxide exhibited defect-free specimen. The
thermal debinding of the alumina feedstock, investigated
in this work, has been successfully carried out under air
atmosphere as can be demonstrated with the SEM pictures
of the final sintered aluminum oxide parts (Fig. 7). The
final porosity of the sintered part is only 1.1305%, which
in terms of the range acceptable for PIM parts (up to 2–
5%) [1].
TGA curves shows (Fig. 6) that during the solvent
debinding (608C, 3 h) there is extracted about 4 wt% of
water-soluble components prior to the thermal process.
During solving, water diffuses into the binder to react
with water-soluble substance, and its molecules diffuse
out of the sample through a network of pores formed by
remaining polymer backbone and alumina particles [39].
Finally, the scanning electron microscopy verifies the
TGA results. Alumina powder well covered with multi-
component binder shown in Fig. 8a is compared with the
state after removal of water-soluble components from the
feedstock (Fig. 8b). At the surface depicted in the Fig. 8c,
the binder is completely removed and the part has an
open presintered porosity.
CONCLUSION
Alumina powder grade for PIM technology was com-
bined with a commercially available multicomponent
binder. An oleic acid was used as modifier to attain suita-
ble viscosity level of 60 vol% feedstock. Rheological,
thermal, PVT, and morphological analyses together with a
proper tailoring of debinding conditions resulted in the
optimization of the production of nonporous homogenous
ceramic parts.
REFERENCES
1. R.M. German and A. Bose, Injection Molding of Metals andCeramics, Metal Powder Industries Federation, Princeton (1997).
2. P. Schwenzel and J.F. Petzold, EuroPM2009 Proc., 2, 129(2009).
3. S. Kurzbeck, J. Kaschta, and H. Munstedt, Rheol. Acta., 35,446 (1996).
4. C.R. Wildemuth and M.C. Williams, Rheol. Acta., 23, 627(1984).
5. N. Casson, ‘‘A Flow Equation for Pigment-oil Suspension of
the Printing Ink-type,’’ in Rheology of Disperse Systems,C.C. Mill, Ed., Pergamon, London, 84 (1959).
6. A.B. Metzner, J. Rheol., 29, 739 (1985).
7. B. Hausnerova, T. Honek, P. Saha, and T. Kitano, J. Polym.Mater., 21, 1 (2004).
8. H.A. Barnes and K. Walters, Rheol. Acta., 24, 323 (1985).
9. H.A. Barnes, J. Non-Newtonian Fluid Mech., 81, 133 (1999).
10. W.H. Herschel and R. Bulkley, Proc. ASTM, 26, 621
(1926).
11. D.M. Husband and N. Aksel, J. Rheol., 37, 215 (1993).
12. B. Hausnerova, P. Saha, J. Kubat, T. Kitano, and J. Becker,
J. Polym. Eng., 20, 237 (2000).
13. B. Hausnerova, P. Saha, and J. Kubat, Int. Polym. Proc., 14,254 (1999).
14. T. Honek, B. Hausnerova, and P. Saha, Appl. Rheol., 12, 72(2002).
15. U. Yilmazer, C.G. Gogos, and D.M. Kalyon, Polym. Comp.,10, 242 (1989).
16. P. Yaras, D.M. Kalyon, and U. Yilmazer, Rheol. Acta., 33, 48(1994).
17. S. Laddha, C. Wu, S. Vallury, G. Lingam, S. Lee, K. Sim-
mons, P. Thomas, B. Levenfeld, A. Varez, S.J. Park, S.
Ahn, R.M. German, and S.V. Atre, PIM Int., 3, 64 (2009).
18. H. Persson, B. Hausnerova, L. Nyborg, and M. Rigdahl, Int.Polym. Proc., 24, 206 (2009).
FIG. 8. Scanning electron micrographs of alumina feedstock after molding (a), water debinding (b), and
solvent/thermal debinding (c).
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19. C.D. Greene and D.F. Heaney, Mater. Des., 28, 95 (2007).
20. W.C.J. Wei, R.Y. Wu, and S.J. Ho, J. Eur. Ceram. Soc., 20,1301 (2000).
21. L.J. Prakash, PIM Int., 1, 17 (2007).
22. R.M. German, PIM Int., 2, 45 (2008).
23. T. Moritz and R. Lenk, PIM Int., 3, 23 (2009).
24. W.W. Yang, K.Y. Yang, M.C. Wang, and M.H. Hon,
Ceram. Int., 29, 745 (2003).
25. R.M. German, Powder Injection Molding, Metal Powder
Industries Federation, Princeton (1990).
26. S.T. Lin and R.M. German, J. Mater. Sci., 29, 5207 (1994).
27. T.Y. Chan and S.T. Lin, J. Am. Ceram. Soc., 78, 2746 (1995).
28. W.J. Tseng, Mater. Sci. Eng. A., 289, 116 (2000).
29. R.L. Hoffman, T. Soc. Rheol., 16, 155 (1972).
30. J.B. Jansma and S. Qutubuddin, J. Rheol., 39, 161 (1995).
31. H.A Barnes, J. Non-Newtonian Fluid Mech., 56, 221 (1995).
32. G.P. Roberts, H.A. Barnes, and P. Carew, Chem. Eng. Sci.,56, 5617 (2001).
33. P. Lomellini and D. Ferri, ‘Polymer Melt Rheology Versus
Shear Rate or Versus Shear Stress?’ in Proc. 13th Int. Con-gress on Rheology, D.M. Binding, N.E. Hudson, J. Mewis,
J.-M. Piau, C.J.S. Petrie, P. Townsend, M.H. Wagner and K.
Walters, Eds., Cambridge (UK), 20–25 Aug 2000, Vol. 1,
pp. 118–120, Published by the British Society of Rheology,
Glasgow 2000.
34. P. Filip, J. David, and R. Pivokonsky, Acta Technica CSAV,51, 349 (2006).
35. J. David and P. Filip, Appl. Rheol., 14, 82 (2004).
36. D.M. Liu and W.J. Tseng, Ceram. Int., 25, 529 (1999).
37. P. Thomas-Vielma, A. Cervera, B. Levenfeld, and A. Varez,
J. Eur. Ceram. Soc., 28, 763 (2008).
38. M. Trunec and J. Cihlar, J. Eur. Ceram. Soc., 17, 203
(1997).
39. V.A. Krauss, A.A.M. Oliviera, A.N. Klein, H.A. Al-Qure-
shi, and M.C.J. Fredel, Mater. Process. Tech., 182, 268
(2007).
1382 POLYMER ENGINEERING AND SCIENCE—-2011 DOI 10.1002/pen