Processing, characterization and biological testing of poroustitanium obtained by space-holder technique
Y. Torres • J. A. Rodrıguez • S. Arias •
M. Echeverry • S. Robledo • V. Amigo •
J. J. Pavon
Received: 27 January 2012 / Accepted: 16 May 2012 / Published online: 30 May 2012
� Springer Science+Business Media, LLC 2012
Abstract The high Young’s modulus of titanium with
respect to that one of the bone is the main cause of the stress-
shielding phenomenon, which promotes bone resorption
around implants. Development of implants with a low
Young’s modulus has gained increased importance during
the last decade, and the manufacturing of porous titanium
is one of the routes to reduce this problem. In this work,
porous samples of commercially pure titanium grade IV
obtained by powder metallurgy with ammonium bicarbonate
(NH4HCO3) as space-holder were studied. Evaluations of
porosity and mechanical properties were used to determine
the influence of compaction pressure for a fixed NH4HCO3
content. Measurements by ultrasound tests gave Young’s
modulus results that were low enough to reduce stress
shielding, whilst retaining suitable mechanical strength.
Biological tests on porous cp Ti showed good adhesion of
osteoblasts inside the pores, which is an indicator of poten-
tial improvement of osteointegration.
Introduction
Among all metallic biomaterials used for bone replace-
ment, titanium and some of its alloys are recognized as the
most successful materials for this purpose [1, 2]. This
success is due to their highly biocompatible behaviour and
their fulfilment of the mechanical requirements of the
application [3–6]. However, their high Young’s modulus
values mean that implants and prostheses do not transfer
the entire applied load to the bone generating a stress-
shielding phenomenon [7–9]. As bone is a dynamic tissue
the structure and density of which are modulated by
applied load, mismatch between the Young’s modulus of
titanium and that of bone generates a loss of bone density,
termed bone resorption [10, 11]. Other factors involved in
stress shielding are implant design, biomechanics and the
biological environment. However, the Young’s modulus of
the implant material is probably the most accessible
parameter to be modified to reduce the problem [1]. Many
failures of titanium implants are associated with fractures
of the surrounding bone and subsequent loosening of the
load-bearing component of the prosthesis. Therefore, it is
desirable to design new implants and prostheses with a
lower stiffness than those currently used, which would
allow the stress-shielding problem to be solved or reduced
without any important detrimental effect on mechanical
strength. Within this context, many research works can
currently be found dedicated to the development of new
implant materials with a bone-matching modulus, such as
metastable b-titanium alloys [12], magnesium and its
alloys [13] and porous materials [14, 15]. There are several
manufacturing processes for the latter, among which are
highlighted: the electron beam melting process [16], creep
expansion of argon-filled pores [17], directional aqueous
freeze casting [18], rapid prototyping techniques [19],
Y. Torres (&) � J. A. Rodrıguez
Department of Mechanical and Materials Engineering,
E.T.S. de Ingenierıa, Universidad de Sevilla, Avda.
Camino de los Descubrimientos, s/n, 41092 Sevilla, Spain
e-mail: [email protected]
S. Arias � M. Echeverry � J. J. Pavon
Biomaterials Research Group, Bioengineering Program,
University of Antioquia, Medellın, Colombia
S. Robledo
PECET, University of Antioquia, Medellın, Colombia
V. Amigo
Departamento de Ingenierıa Mecanica y de Materiales,
Universidad Politecnica de Valencia, Camino de Vera s/n,
46022 Valencia, Spain
123
J Mater Sci (2012) 47:6565–6576
DOI 10.1007/s10853-012-6586-9
laser-engineered net shaping [20], electric current acti-
vated/assisted sintering techniques [21, 22], conventional
powder metallurgy [23] and space-holder techniques [24].
In this last process, most of the space-holders (ammonium
bicarbonate [25–28], carbamide [29] and PVA [30]) are
completely evaporated at low temperatures, whilst others
(e.g., sodium chloride [31–35]) are removed by a dissolu-
tion process, generally in water.
Space-holder techniques offer a route to controlling
porosity parameters such as pore morphology and per-
centage. Important efforts and advances within this field
are widely recognized [36]. Most of these works have
focused on the influence of processing conditions on
porosity parameters [24, 29, 37, 38], as well as on the
mechanical response to uniaxial compression [26, 29, 39].
A few of them have studied other interesting properties
such as fracture [27], fatigue [28] and biological testing
[40–42]. These previous manuscripts have not assessed
the overall relationship between the above properties:
processing, microstructure, mechanical and biological
behaviour.
The aim of this work is to evaluate the influence of
compaction pressure on both mechanical properties and the
results of in vitro biological testing of porous cp Ti samples
manufactured by space-holder technique. Samples were
fabricated by a non-conventional powder metallurgy (PM)
process using NH4HCO3 as space-holder. Some process
conditions were fixed according to previous works by the
authors [43]: space-holder content and the procedure for its
elimination, as well as sintering time and temperature. The
influence of different compaction pressures was evaluated
through changes in microstructural and mechanical behav-
iour (yield strength, conventional and dynamic Young’s
modulus) and, finally, the samples were biologically tested
to determine their osteointegration potential.
Materials and methods
Processing of samples
The commercially pure Titanium (CP Ti) powder
(SE-JONG Materials Co. Ltd., Korea) used for the blends
was manufactured by a hydrogenation/dehydrogenation pro-
cess. The particle size distribution corresponded to 10, 50
and 90 % passing percentages, of 9.7, 23.3 and 48.4 lm,
respectively. The chemical composition of the powder used
was equivalent to CP Ti Grade IV according to the ASTM
F67-00 Standard [44]. CP Ti has an apparent density
of 1.30 ± 0.01 g/cm3 (28.8 ± 0.1 %) and a tap density
of 1.77 ± 0.04 g/cm3 (39.2 ± 0.8 %). Its morphology is
approximately equiaxial and its surface is very rough
(Fig. 1). The ammonium bicarbonate particles (NH4HCO3,
Cymit Quımica S.L, Spain) employed as space-holder, has
a particle size corresponding to 10, 50 and 90 % passing
percentages of 73, 233 and 497 lm, respectively, with a
purity of 99.9 %. The initial NH4HCO3 was sieved up to a
range between 100 and 200 lm to obtain a homogeneous
pore size. NH4HCO3 powder has an apparent density of
0.738 ± 0.01 g/cm3 (46.5 ± 0.1 %) and a tap density of
0.87 ± 0.04 g/cm3 (54.83 ± 0.8 %) (Fig. 1). The blends
of CP Ti powder and NH4HCO3 granules [CP Ti ?
NH4HCO3], with a NH4HCO3 concentration of 50 vol.%,
were prepared using a Turbula� T2C blender for 40 min to
ensure good homogenization. This NH4HCO3 content was
chosen according to the previous works by the authors with
conventional PM [35] and space-holder results with NaCl
[45] based on the optimum porosity to match the Young’s
modulus of cortical bone. The compacting step was carried
out using an Instron 5505 universal machine to apply the
pressures used (200, 400, 600 and 800 MPa). The com-
pacting loading rate was 6 kN/s, dwelling time was 2 min
and unloading time was 15 s for decreasing load up to
150 N. Elimination of NH4HCO3 from green samples
was performed thermally by placing the samples in an
oven at 100 �C for 10 h. The sintering process was per-
formed in a Carbolyte� STF 15/75/450 ceramic furnace
with a horizontal tube at 1250 �C for 2 h using high vac-
uum (*5�10-5 mbar). Diameter of compaction die (8 mm)
and powder mass were selected to obtain samples in which
the effect of compaction pressure was minimized [35].
These parameters were kept constant for compression tests
(height/diameter = 0.8 [46]).
Density and porosity characterization
Density measurement was carried out by the Archimedes’
method with distilled water impregnation. This method was
chosen for its experimental simplicity and reasonable
reliability (ASTM C373-88 [47]). This method basically
consisted of: (1) weighing the dry sample, (2) warming the
sample in distilled water for 5 h, (3) leaving the sample for
24 h (to ensure that water penetrates through the porosity),
(4) removing the sample and letting the outer water drain
off, (5) weighing the sample again (mass of saturated
sample), (6) once again, weighing the sample immersed in
water. The total and interconnected porosity were calcu-
lated from density measurements. Three specimens were
employed for each material and three measurements were
made per each sample (9 for each material). The porosity
evaluation by image analysis (IA) was performed using a
Nikon Epiphot optical microscope coupled with a Jenoptik
Progres C3 camera and suitable analysis software (Image-
Pro Plus 6.2). Before the image analysis, the sectioned
parts were prepared by a sequence of conventional steps
(resin mounting, grinding and polishing) followed by a
6566 J Mater Sci (2012) 47:6565–6576
123
mechanochemical polishing with magnesium oxide and
hydrogen peroxide. Image analysis was assessed using 10
pictures of 59 for each sample (one for each kind of
material). The main porosity characteristics estimated by
this method were: (i) the pore shape factor (Ff = 4pA/PE2,
where A is the pore area and PE is the experimental
perimeter of the pore) [48]; (ii) the mean free path between
the pores (k, measure of the mean size of titanium matrix.
This parameter is calculated in the same way as cemented
carbide [49]); (iii) the equivalent diameter (Deq) [48]; and
(iv) the porosity itself.
Mechanical testing
For mechanical compression testing, the specimen dimen-
sions were fixed according to those recommended (height/
diameter = 0.8) in Standard ASTM E9-89a [46]. The tests
were carried out using a universal electromechanical Instron
machine 5505 by applying a strain rate of 0.005 mm/
mm min. All tests were run up to a strain of 50 % and,
afterwards, both Young modulus, E, and yield strength, ry,
were estimated. The Young’s modulus estimation from the
compression stress–strain curves was corrected by including
testing machine stiffness (87.9 kN/mm). Three specimens
were employed for each space-holder percentage. These
tests were performed on the samples in which porosity
(density) and dynamic Young’s modulus were already
measured. Measurement of dynamic Young’s modulus was
performed by an ultrasound technique using a Krautkramer
USM 35� flaw detector. This method allowed both the lon-
gitudinal and transverse propagation velocities of acoustic
waves to be determined. To evaluate the longitudinal waves,
a Panametric S-NDT� 4 MHz ultrasonic transducer was
used with an ultrasonic couplant (Sonotrace grade 30�). For
transverse waves, a Panametric S-V153� 1.5 MHz shear
wave transducer was used using a shear wave couplant
(Panametrics-NDT(TM)). The Metals Handbook section on
non-destructive evaluation and quality control [50] was used
as a reference and includes the results of measurements on
nonporous CP Ti samples corresponding to velocities of
longitudinal and transverse waves of 6.1 and 3.12 km/s,
respectively. Wave velocities through porous samples were
measured by minimizing delay times of transducers fol-
lowing an iterative measurement protocol. Mathematical
Fig. 1 Raw powder materials. a, b Ti; c, d NH4HCO3. a, c represent a general view and b, d are detailed images from the surfaces. It is
remarkable to notice the superficial roughness of both Ti and NH4HCO3 powder
J Mater Sci (2012) 47:6565–6576 6567
123
expression was employed to calculate the dynamic Young’s
modulus once the acoustic wave velocities were measured
(see Eq. 1, [51]). This equation has been used by other
authors [52] and their experimental results were consistent
with poro-micromechanical model predictions based on the
stiffness and strength properties of pure titanium and on the
specific porosity of the sample.
Ed ¼ qv2
T 3v2L � 4v2
T
� �
v2L � v2
T
ð1Þ
where q is the density (g/cm3) and VL and VT are the
longitudinal and transverse velocities, respectively.
In vitro biological testing
The samples were sterilized in water steam at a pressure of
2300 mbar at 121 �C before cytotoxicity and cell mor-
phology tests. These were performed using an osteoblast
cell line SAOS-2 (ATCC, USA). Before testing, the cells
were cultured in culture bottles and grown for 72 h in an
incubator at 37 �C with 5 % CO2. The culture media was
prepared with 10 % foetal bovine serum (FBS) and 90 %
McCoy’s medium (Sigma-Aldrich). Cytotoxicity and cell
morphology tests were both based on the protocol descri-
bed by Denizot et al. [53] and adapted by Echeverry [54].
Porous Ti samples were placed in a culture plate of 48
wells, two of which were used for cytotoxicity-positive
controls and which would contain only culture media and
cells. Osteoblasts were then harvested by adding 0.05 %
trypsin (Sigma) to culture bottles with suitable cell densi-
ties (for 10 min at 37 �C). The cell suspensions were then
decanted into centrifuge tubes and spun at 1300 rpm, for
10 min, to obtain a precipitate. Each Ti sample was then
seeded in a cell suspension (500000 cells/mL) and incu-
bated at 37 �C for 72 h. Cell viability was determined by
the yellow tetrazolium MTT (Sigma) method. The stop
solution consisted of 10 % sodium dodecyl sulphate
(Fischer, USA) and 50 % isopropanol. Production of for-
mazan was determined using a microplate reader (Bench-
mark, Biorad) at 570 nm. Results were expressed as the
cell death percentage. Regarding the cell morphology, the
cell suspension for seeding was obtained by following a
similar protocol as for cytotoxicity; however, in this case, a
concentration of 10000 cells/cm2 was used for each sam-
ple. The seeded samples were incubated at 37 �C for 72 h.
Osteoblasts were then fixed in the material with 2 % glu-
taraldehyde for 12 h at 4 �C. Cell dehydration was
achieved with increasing concentrations of ethanol (30, 50,
70, 80, 90 and 100 %) in phosphate buffered saline (PBS).
Finally, the samples were subjected to critical point drying
and coated with gold to be observed by scanning electron
microscopy (SEM).
Results and discussion
Density and porosity characterization
Porous samples were structurally stable during the whole
process for all the compaction pressures used. Table 1
shows that both total and interconnected porosity for the
whole compaction pressure range were always lower than
the nominal space-holder content (50 vol.%) and those
porosities were slightly higher as the compaction pressure
was increased. This difference with respect to nominal
space-holder content is assumed to be a consequence of
several facts: a higher compaction pressure implies a more
severe plastic deformation of the space-holder, which
allows the coalescence between pores, and therefore, a
higher interconnected porosity; this makes space-holder
elimination easier. Besides this, there is a normal porosity
reduction after sintering, with respect to the nominal one,
which is a well-known phenomenon in both PM and space-
holder practice; it is assumed to be a consequence of
metallic framework shrinkage during sintering, which gen-
erates a reduction in surface energy of particles [37, 55, 56].
This same phenomenon has been observed and discussed
by the authors in a previous work with NaCl as space-
holder [45]. Water content of the space-holder can also
have a small influence on porosity reduction with respect
to initial NH4HCO3 percentage. The slight increment
in the interconnected porosity (36.3–39.9 vol.%) as the
compaction pressure is increased confirms the above
mentioned mechanism because it promotes the coalescence
of pores.
Mechanical testing
The evaluation of Young’s modulus in porous materials is
controversial. Young’s modulus measurements from uni-
axial compression tests are significantly lower than
dynamic measurements. Greiner et al. [57] associated this
discrepancy to super-elastic deformation within the linear-
elastic range of NiTi materials; stiffness measured by
Table 1 Total and interconnected porosity as a function of com-
paction pressure
Powder
metallurgy
process
Compaction
pressure (MPa)
Porosity (%)
Total Interconnected
Space-holder 200 42.8 ± 2.6 36.3 ± 0.4
400 44.1 ± 2.5 37.6 ± 1.3
600 44.7 ± 2.5 38.5 ± 0.3
800 45.0 ± 2.5 39.9 ± 0.2
Conventional 0 41.5 ± 2.5 40.0 ± 0.3
211.5 7.2 ± 2.5 1.9 ± 0.1
6568 J Mater Sci (2012) 47:6565–6576
123
ultrasonic technique decreases with increasing porosity
in agreement with Eshelby’s elasticity-based theory for
closed, spherical porosity. We reported a similar trend for
C.P. Ti obtained by a conventional powder-metallurgy
process [35], as well as in recent work [45] developed with
space-holder (NaCl). These authors related this difference
to the testing machine stiffness in which the mechanical
system and sample were considered as two springs in
series. Moreover, it must be remembered that Ti matrix is
different at each cross section of the cylindrical sample
during a compression test; the material collapse starts at the
section with the lowest Ti content. In works such as those
mentioned above, the reliability and certainty of ultrasound
measurements were validated by comparison with a well
known and accepted pore-elasticity model, such as that of
Nielsen [58].
Initially, influence of testing machine stiffness on the
Young’s modulus evaluations by uniaxial compression
tests was determined. From stress–strain curves (see Fig. 2)
and Young’s modulus measurements with ultrasound tech-
nique (Table 2), it can be observed that increments of
compaction pressure reduce both Young’s modulus and
yield strength with a reduction in the latter. The Young’s
modulus reduction by ultrasound technique is less marked
and even it can be assumed to keep approximately con-
stant (24.63 ± 1.4–24.11 ± 1.5 GPa) because such a small
porosity reduction does not have a strong influence on the
total stiffness of the sample. However, the influence of
compaction pressure on yield strength is clearly greater
(215 ± 11–174.5 ± 6.6 MPa) because this mechanical prop-
erty is sensitive to other parameters besides porosity: neck
strength, pore shape factor, equivalent diameter of pores
and mean separation between pores. With respect to the
influence of intrinsic neck strength, it is normally assumed
that this parameter is greater as the compaction pressure is
increased; this is associated with a breakdown of the oxide
layer and the consequent promotion of a cold welding
effect between particles and subsequent better diffusion
during the sintering. However, from Table 2, it seems that
this is not the case. From Table 2, it is observed that
Young’s modulus and yield strength of space-holder sam-
ples are between those from loose sintering and conven-
tional PM with 211.5 MPa of compaction pressure. This
comparison confirms role of porosity obtained by space-
holder technique.
The pore shape factor, Ff, is more related to influences
on both mechanical strength and fatigue life, as well as in
the case of mean separation between pores, k. Results in
Table 3 are consistent with the expected influence of Ff on
yield strength (greater yield strength values for greater Ff
values). However, k behaviour does not show a significant
role on yield strength. On the other hand, evaluation of the
equivalent diameter of pores, Deq, as compaction pressure
was increased (200–800 MPa) for NH4HCO3 contents
between 30 and 70 vol.% showed increments between 30
and 40 % (Table 3). This latter trend is clearly consistent
with the fact that a smaller pore size indicates greater yield
strength. In summary, despite all the above, the mentioned
parameters are expected to influence mechanical strength;
in this case, dominant role of pore shape factor and
equivalent diameter (pore size) explain the observed behav-
iour of yield strength for increased compaction pressure.
Therefore, the influence of pore equivalent diameter and
pore shape factor can be considered important enough to
affect yield strength in addition to the evident diminishing
effect due to the total and interconnected porosity. It should
be pointed out that this whole line of reasoning was devel-
oped by considering that time and sintering temperatures
were fixed variables, which are well known to have a clear
effect on the mechanical strength of the final PM samples.
Concerning the cortical bone replacement (E * 20
[59, 60]), the best stiffness result measured by ultrasound
technique (24.09 ± 1.5–24.11 ± 1.51 GPa) corresponded
to a space-holder content of 50 % (45 % porosity) for
compaction pressures between 600 and 800 MPa. How-
ever, once the match with Young’s modulus of cortical
bone is considered, it is also important to highlight the
sample which offers a better mechanical balance between
stiffness and strength. In that sense, the best sample was the
one with 50 vol.% of NH4HCO3 (42.8 % porosity) for
200 MPa of compaction pressure: E = 24.63 ± 1.46 GPa
and ry = 215 ± 11 MPa (Cortical bone, ry = 150 MPa).
Despite this optimum value of yield strength being rela-
tively close to that of cortical bone, bigger pores (larger
than 50 lm [61], 100 lm [62–65] and even 150 lm [66]),
Fig. 2 Compression stress–strain curves and yield strength values for
different compaction pressures. Every curve corresponds to a single
run test between carried out for every compaction pressure. The
concerning mean and dispersion values for every batch are shown in
Table 2
J Mater Sci (2012) 47:6565–6576 6569
123
will help bone ingrowth into the porous sample, which will
partially reduce the risk of fatigue failure.
In vitro biological testing
Cytotoxicity results were expressed as cell death percent-
ages, according to a simple calculation from the different
absorbance signals from a Biorad reader [54]. Most of the
samples presented cell death percentages lower than 25 %,
which indicates that they are not potentially toxic. How-
ever, some other samples presented a higher value of cell
mortality because of their interconnected porosity, which
allowed cells to settle at the bottom of the recipient; this
fact partially prevents a complete cell recovery to be
accomplished, as will be discussed later in this paper (see
Fig. 3).
Figure 4 summarizes the morphology and cell adhesion
behaviour in samples with increased compaction pressure.
It should be noted that all samples exhibit good osteoblast
adhesion inside the pores, indicating an important osteo-
integration potential.
Morphological details of the cells inside the pores are
diverse and they depend on the topographical features of
that inner surface (see Fig. 5). Osteoblasts on all samples
seem to be well attached to peaks inside the pores or
between depressions, which are separated by a length
similar to osteoblast diameter (*10 lm); this feature is
more clearly observed with the lowest compaction pres-
sure. For some of these inner surfaces, cells presented a
high dorsal surface activity with small diameter cytoplas-
mic extensions, which appear to spread up to the highest
peaks of the surface. The cell morphology becomes wide-
spread with fewer small diameter extensions, as the rough-
ness peaks become more separated and smaller, which
correspond to increasing compaction pressure. Increments
in compaction pressure reduce cell adhesion because the
space-holder becomes more flat as compaction pressure is
Table 2 Mechanical properties estimated from uniaxial compression tests and ultrasound technique
Powder metallurgy process Compaction pressure (MPa) Sintering
(�C, h)
Young’s modulus (GPa) Yield strength
(MPa)Uniaxial compression test Dynamic (ultrasound
technique)Uncorrected Corrected
Space-holder 200 1250; 2 4.5 10.6 ± 2.2 24.6 ± 1.4 215 ± 11
400 5.1 2.7 ± 1.6 24.8 ± 1.6 188 ± 10
600 3.1 8.5 ± 1.8 24.1 ± 1.5 192 ± 8
800 3.1 9.3 ± 1.8 24.1 ± 1.5 174.5 ± 6.6
Conventional 0 1000; 2 3.4 9.6 ± 1.6 23.9 ± 1.8 68 ± 6
211.5 1300; 2 8.8 59.5 ± 2.1 105.4 ± 1.1 620
Measurements errors correspond to standard deviation. Note: yield strength and Young’s modulus for bulk Ti are 650 MPa and 110 GPa,
respectively
Table 3 Microstructural
parameters as a function of
space-holder content and
compaction pressure
Powder metallurgy process Compaction
pressure (MPa)
Deq (lm) Ff k (lm)
Space-holder vol.% 30 200 14 ± 29 0.94 ± 0.15 46.3 ± 85.9
800 18 ± 38 0.93 ± 0.16 56.5 ± 101.9
70 200 38 ± 71 0.81 ± 0.23 48.5 ± 88.0
800 53 ± 97 0.75 ± 0.24 58.7 ± 101.6
Conventional 0 16 ± 17 0.74 ± 0.30 32.8 ± 28.7
211.5 13 ± 15 0.84 ± 0.21 161.7 ± 131.2
Fig. 3 Cytotoxicity results presented as cell death in terms of
compaction pressure
6570 J Mater Sci (2012) 47:6565–6576
123
increased. Therefore, once the space-holder is removed, the
inner surface of pores will be smoother. This mechanical
response of the space-holder to increasing compaction
pressures is a consequence of its very low fracture tough-
ness related to its high water content associated with its
hygroscopic behaviour; these facts are responsible for its
plastic-like behaviour under pressure. These results are
consistent with the work of Laptev et al. [37] in which they
found that 50 % NH4HCO3 was the critical content at
which it started to respond in a highly plastic manner as a
lubricant was not necessary for the ejection of green
samples. For comparison purposes, it can be seen that the
inner surfaces of pores of a loose-sintering sample (no
compaction pressure, no space-holder) appear very smooth
(Figs. 6a, 7a).
It is also interesting to note that cell death behaviour in
Fig. 3 can be considered consistent with the better cell
adhesion mentioned above: samples obtained with the
Fig. 4 SEM micrographs of osteoblast morphologies inside the pores for different compaction pressures: a Image of an osteoblast on a simply
machined monolithic Ti sample; b 200 MPa; c 400 MPa; d 600 MPa; e 800 MPa
J Mater Sci (2012) 47:6565–6576 6571
123
lowest compaction pressure show the highest cell death
percentage despite them having less interconnected porosity
(Table 1).
The better cell morphologies observed suggest that
parameters associated with roughness inside the pores are
close to those recognized as improving cell adhesion: for
Boyan and Swartchz [67], cells sense the roughness when
the peak height is higher than 2 lm and lower than the cell
diameter (10–20 lm), as well as for a separation between
peaks no longer than the cell diameter. In a later work,
Aparicio et al. [68] showed more restricted values of these
parameters for optimal osteoblast adhesion for a roughness
obtained by sandblasting with alumina particles: mean
height of peaks (vertical parameter), Ra = 4–5 lm, and
mean separation between peaks (horizontal parameter),
Sm = 70–80/cm. It must be noted that osteoblast mor-
phology on a simply machined monolithic Ti sample pre-
sents a typical rounded shape, indicating a poor cell
adhesion to the substrate (Fig. 4a).
Results of cell adhesion observed in Figs. 4 and 5 are
partly consistent with those desired values of surface
roughness: Ra parameter seems to be within the optimum
values; however, it is appreciated that separation between
peaks is similar to cell diameter (a higher Sm parameter)
which is different to what was reported by the above
authors. The good adhesion results, despite a longer sepa-
ration between peaks, could be explained in terms of sur-
face curvature inside the pores: this factor can play an
important role in cell adhesion and it is not present when
the tested surface is flat, as was the case in the works of the
above authors. However, the real influence of surface
curvature on cell adhesion must be the subject of a detailed
evaluation in a separate study and this will be a subject of
future works.
Cell behaviour observed in Figs. 4 and 5, indicates
that, as compaction pressure is increased, inner roughness
of pores deviates with respect to desired values and cells
become more flat, exhibiting a fibroblast-like behaviour
(less osteoblastic) with a clearly less adhesive force. The
high dorsal activity of cells attached to rough surfaces is
also an indicator of the active state of cell phenotype
development that is, at the same time, an indicator of a
better differentiation response of osteoblasts. Interestingly,
the better cell adhesion results obtained in this work
Fig. 5 SEM micrographs showing details of osteoblast adhesion inside the pores for different compaction pressures: a 200 MPa; b 400 MPa;
c 600 MPa; d 800 MPa
6572 J Mater Sci (2012) 47:6565–6576
123
(compaction pressure of 200 MPa) are coincident with
samples of the best mechanical balance for cortical bone
replacement: E = 24.6 GPa and ry = 215 MPa. How-
ever, it must be mentioned that reaching a complete
mechanical balance will require a detailed fatigue evalu-
ation in which case inner roughness of pores for samples
compacted with 200 MPa could have some influence.
This is part of current research that the authors will be
submitting soon.
Conclusions
Once the influence of compaction pressure for a fixed
space-holder content (NH4HCO3) designed for porous
titanium implants was evaluated, the following conclusions
were drawn:
• Total and interconnected porosity of samples for the
whole compaction pressure range were always lower
Fig. 6 SEM micrographs of porosity behaviour for different compaction pressures: a porosity of a conventional PM sample, loose sintering at
1300 �C for 2 h; b 200 MPa; c 400 MPa; d 600 MPa; e 800 MPa
J Mater Sci (2012) 47:6565–6576 6573
123
than nominal space-holder content; both kinds of
porosities were higher as the compaction pressure was
increased. This porosity behaviour is assumed to be a
consequence of severe plastic deformation of space-
holder as compaction pressure is increased.
• Mechanical testing showed that increments of compac-
tion pressure slightly reduce Young’s modulus because
such a small porosity reduction does not have a strong
influence on it. Significant reduction of yield strength
with compaction pressure can be explained because this
mechanical property is especially sensitive to the
equivalent diameter of pores. This parameter presents
increments between 30 and 40 %, which is large
enough to influence yield strength, in addition to an
evident diminishing effect on total and interconnected
porosity.
• The optimum balance of mechanical properties with
respect to cortical bone was achieved in a sample with
42.8 % porosity and 200 MPa of compaction pressure:
E = 24.6 GPa and ry = 215 MPa. Both the percentage
Fig. 7 SEM micrographs showing roughness inside the pores for different compaction pressures: a porosity of a conventional PM sample, loose
sintering at 1300 �C for 2 h; b 200 MPa; c 400 MPa; d 600 MPa; e 800 MPa
6574 J Mater Sci (2012) 47:6565–6576
123
of big pores (larger than 50, 100 lm and even 150 lm)
and the interconnected porosity achieved are factors
that can improve the ingrowth of cortical bone through
the porous implants, partially reducing the risk of
fatigue failure.
• Cytotoxicity tests showed that all porous samples were
non-toxic, which validates the biological viability of all
processing conditions. Biological tests also showed
osteoblast behaviour inside residual pores from a space-
holder technique. The osteoblast morphologies at all
compaction pressures were considered to be promising
for improving osteointegration of titanium implants.
The attachment force of cells is better for rougher inner
surfaces of the pores, i.e., increments in compaction
pressure reduce cell adhesion because the space-holder
becomes more flat as compaction pressure is increased.
In that sense, the better cell adhesion results obtained in
this work (compaction pressure of 200 MPa) are
coincident with samples with the best mechanical
balance for cortical bone replacement: E = 24.6 GPa
and ry = 215 MPa.
• The optimum behaviour of samples obtained in this
work with lowest compaction pressure (200 MPa), with
50 vol.% NH4HCO3, indicates that it is a promising
route for developing titanium implants with a high
cellular adhesion (improved osteointegration), suitable
bone ingrowth and a clearly reduced stress shielding
with a reasonably good mechanical strength.
Acknowledgments This work was supported by the Ministerio de
Ciencia y Tecnologıa, MICINN (Spain) through the project Ref.
MAT2010-20855. Furthermore, the authors want to thank laboratory
technicians J. Pinto and M. Sanchez, and the undergraduate student I.
Nieto for their assistance in microstructure characterization and
mechanical testing.
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