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## Journal of the Brazilian Society of Mechanical Sciences and Engineering

##
*versión impresa* ISSN 1678-5878

### J. Braz. Soc. Mech. Sci. & Eng. vol.33 no.3 Rio de Janeiro jul./set. 2011

#### http://dx.doi.org/10.1590/S1678-58782011000300009

**TECHNICAL PAPERS MANUFACTURING PROCESS**

**Improvement of Soft Tooling Process Through Particle Reinforcement with Polyurethane Mould**

**Arup Kumar Nandi ^{I}; Shubhabrata Datta^{II}**

^{I}Central Mechanical Engineering Research Institute (CSIR-CMERI), Advance Design and Optimization, 713209 Durgapur, West Bengal, India, nandiarup@yahoo.com

^{II}Birla Institute of Technology, Deoghar, 814142 Deoghar, Jharkhand, India, sdatt@bitmesra.ac.in

**ABSTRACT**

Use of conventional flexible polymeric mould materials yields to longer solidification time of (wax/plastic) patterns in soft tooling process, thereby reducing the rapidity of the process to a great extent, which is not desirable in present competitive market. In this work, approach of particle-reinforcement with mould materials is introduced to reduce the cycle time of Soft tooling process and the resulting cooling time is experimentally investigated in considering a case of manufacturing of a typical wax pattern with aluminium particle filled polyurethane. It is observed that cooling time is significantly reduced particularly with higher loading condition of aluminium filler. This happens due to the increase of effective thermal conductivity of mould material. However, it is also found that the stiffness of mould becomes simultaneously high due to increase of effective modulus of elasticity of mould material. Realizing these facts, an extensive study is carried out to find the effect on equivalent thermal properties and modulus of elasticity of polyurethane composite mould materials with the reinforcement of aluminium and graphite particles independently through rigorous experimentation and correlation of experimental findings with the models cited in literatures.

**Keywords:** soft tooling process, flexible polymeric mould material, particle reinforcement, cooling time, equivalent thermal conductivity, equivalent modulus of elasticity

**Introduction**

Among different rapid tooling processes, soft tooling (ST) is the one where polymeric flexible materials are used for making mould (Rosochowski and Matuszak, 2000). ST process is particularly suitable to produce wax patterns in small batch by vacuum assisted or gravity casting method based on RP (rapid prototype)/others pattern. This wax component is used in investment casting process as a pattern to make ceramic slurry and finally metallic components are produced by fusing the wax pattern. Development of metal component through rapid prototyping (RP)-soft tooling-investment casting process is illustrated in Fig. 1.

**Nomenclature**

| = | maximum packing fraction of disperse phase |

| = | thermal diffusivity, mm^{2}/sec |

| = | thermal conductivity, W/m-k |

| = | thermal conductivity in x-direction, W/m-k |

| = | thermal conductivities in z direction, W/m-k |

ρ | = | density of material |

| = | specific heat of material |

| = | temperature at point (x, y, z) and time, t |

| = | amount of heat released at (x, y, z, t) per unit volume and unit time, J/m^{3}-s |

| = | power output of hot disk sensor per unit time |

| = | heat released per unit length of hot disk sensor ring source, J/m^{3}-s |

| = | Dirac delta function |

| = | radius of the largest ring of concentric spiral hot disk sensor, mm |

| = | half thickness of concentric spiral hot disk sensor, µm |

| = | number of concentric rings of spiral hot disk sensor |

| = | total length of rings of spiral hot disk sensor, mm |

| = | an integration variable |

| = | characteristic time ratio (dimensionless parameter) |

| = | dimensionless time function |

| = | average temperature increase of hot disk sensor |

| = | thermal conductivity of composite, W/m-k |

| = | thermal conductivities of polymer/matrix, W/m-k |

| = | thermal conductivities of filler material, W/m-k |

| = | Einstein coefficient |

φ | = | volumetric fraction of filler in the composite |

| = | modulus of elasticity, N/mm^{2} |

| = | shear modulus, N/mm^{2} |

| = | bulk modulus, N/mm^{2} |

| = | modulus of elasticity of matrix/polymer, N/mm^{2} |

| = | modulus of elasticity of filler material, N/mm^{2} |

| = | modulus of elasticity of composite, N/mm^{2} |

| = | shear modulus of matrix/polymer, N/mm^{2} |

| = | shear modulus of filler material, N/mm^{2} |

| = | shear modulus of composite, N/mm^{2} |

| = | bulk modulus of matrix/polymer, N/mm^{2} |

| = | bulk modulus of filler material, N/mm^{2} |

| = | bulk modulus of composite, N/mm^{2} |

| = | lower bound of modulus of elasticity, N/mm^{2} |

| = | upper bound of modulus of elasticity, N/mm^{2} |

= | Hashin-Shtrikman lower bound of bulk modulus, N/mm^{2} | |

= | Hashin-Shtrikman upper bound of bulk modulus, N/mm^{2} | |

= | Hashin-Shtrikman lower bound of shear modulus, N/mm^{2} | |

= | Hashin-Shtrikman upper bound of shear modulus, N/mm^{2} | |

| = | polyurethane |

| = | aluminium |

| = | rapid prototyping |

| = | soft tooling |

| = | stereo-Lithography Apparatus |

| = | thermal conductivity |

| = | equivalent thermal conductivity |

TPS | = | transient plane heat source |

The common polymeric flexible mould materials used in soft tooling process are polyurethane (PU), silicone rubber, etc. However, the conventional mould materials possess poor thermal conductivity (TC). Therefore, the solidification time of wax/plastic pattern produced in ST process is long because of poor heat flow rate through the mould wall. As a result, the rapidity of soft tooling process is reduced to a great extent. In order to increase the heat flow rate through mould wall, enhancement of thermal conductivity of mould material is an essential issue which can be achieved either by molecular orientation of polymeric mould material itself in order to synthesize new (highly conductive) polymeric material or by the reinforcement of high conductive fillers into existing mould materials. In the present work, approach of particle-reinforcement with existing mould materials is adopted, because reinforcement of conductive fillers (particularly in the form of particles) into the mould material is the simplest method that may be easily implemented in practical application. Furthermore, the degree of increasing effective thermal conductivity and other mould properties can be easily controlled by deciding proper amount of filler content in the polymer. The resulting cooling time in ST process is experimentally investigated in considering a case of manufacturing of a typical wax pattern with aluminium filled polyurethane.

Through experimentation, it is observed that cooling time is significantly reduced particularly with higher loading condition of aluminium filler, due to the increase of effective thermal conductivity of mould material. But simultaneously it is also found that the stiffness of mould becomes high due to increase of modulus of elasticity of mould material. High stiffness of mould is not desirable in soft tooling process, because releasing pattern and wax component from the mould box becomes difficult. Therefore, it is important to carry out an extensive experimental study to find the effect on equivalent thermal properties and modulus of elasticity of polyurethane composites by reinforcing aluminium and graphite particles independently with different loading conditions.

A significant amount of research works was found where particulate filler materials were introduced in polymer to increase its effective thermal conductivity (Agrawal et al., 2000; Boudenne et al., 2004; Miller et al., 2006; Mu, Feng and Diao, 2007; Subodh et al., 2008; Vinod, Varghese and Kuriakose, 2004; Sundstrom and Chen, 1970; Kim et al., 2008; Pal, 2007). The equivalent thermal conductivity (ETC) of particulate filled polymer composites was also investigated with the variation of various morphological properties of conductive filler particles (Ye, Shentu and Weng, 2006), multi-modal particle size mixing (Yung and Liem, 2007) as well as using hybrid filler materials (Lee et al., 2006). Moreover, addition of filler particles in mould material increases the effective modulus of elasticity of mould materials (Tavman, 1997; Rusu, Sofian and Rusu, 2001; Papanicolaou and Bakos, 1992).

In the present work, equivalent thermal and mechanical properties of particle reinforced polyurethane composites are analysed through rigorous experimentation. In addition, various predictive models of equivalent thermal conductivity and modulus of elasticity reported in the literature are tried to validate based on the experimental results which will be highly helpful in industry for estimation of time requirement for manufacturing a component in ST process.

The rest of the article is organized as follows: the second section describes the materials and morphology of filler particle. Details of experimentation with results of cooling time in ST process are presented in the third section. Measurement procedures, discussions on experimental results and validation of model(s) of equivalent thermal conductivity and modulus of elasticity of Al and graphite particle reinforced polyurethane are illustrated in the fourth and fifth sections, respectively. Finally, concluding remarks are drawn in the sixth section.

**Flexible Mould Material and Particulate Fillers**

**Flexible mould materials **

In the present study on the effect of cooling time in ST process using particle reinforcement with flexible mould materials, we have considered polyurethane (of type PMC 121/50) produced by Smooth-ON, Inc. USA. The polyurethane (PU) mould material has two parts, Part A (liquid polymer) and hardener/Part B. Both Part A and Part B are mixed in the ratio of 1:1 either in weight or volume and normally cured in room temperature. The value of thermal conductivity (kp) of cured PU mould material as experimentally found is 0.1615 W/m-k.

**Filler particle**

The filler materials, aluminium fine powder and graphite granules having thermal conductivities 237 and 209.34 W/m-k, respectively, are taken in this study. Measurements of granulometric parameters of both the fillers are made using M420, WILD Heerbrugg Microscope. The particle size and shape distributions of both filler materials are enlisted in Table 1. The (arithmetic mean) size of particles is determined by taking the average of minimum and maximum lengths of the particles. For (near) spherical shape, the particle size is equivalent to the diameter of sphere. For (near) cylindrical shape, the size of particle is equal to (length + diameter)/2. In order to find the size distribution of particles, a small amount of sample is taken at random form bulk. We have counted the number of particles in that amount as well as measured the size of each particle in an approximate approach and finally determined the particle size distributions arithmetically in four different ranges. The average particle sizes (calculated based on weighted average method) of aluminium and graphite fillers are 12.3 micron and 296 micron, respectively. The maximum volume fractions of graphite and aluminium particles found experimentally are 0.5216 and 0.6032, respectively.

**Experimentation of Cooling Time in ST Process **

The effect of cooling time in soft tooling process using particle reinforced mould material is experimentally investigated. In this experimental study, we have considered PU as mould material and Al particle is taken as filler material. We have compared the cooling time required using Al filled PU composite mould material with that of using only PU for producing a cubical shaped (size: 50 mm x 50 mm x 50 mm) wax component. The experimentation is carried out with the amounts of Al filler content in PU mould material as 23.8% of volume fraction.

**Wax material**

In the present study, Investment casting wax (A7-11) supplied by Blayson Olefines Ltd, UK, is used. The wax consists of natural wax, synthetic wax and natural resins. The melting point of wax is 55ºC-70ºC and the boiling point/flash point is greater than 200ºC. The melt wax possesses viscosity of 0.6 Pas at around 100ºC.

**Preparation of mould and manufacturing of wax component**

A cubical shaped RP component made using Stereo Lithography Apparatus (SLA) is used as a pattern for making the mould. The pattern is finished to a desired quality as required for the final wax component. The RP pattern is suspended by Teflon rod in an enclosed box (using thin sheet preferably made of Perspex material) and necessary arrangement is made to provide passage in the mould box for pouring the molten wax into the mould box. The weights of part-A and part-B of liquid PU and Al filler are calculated based on the respective densities of these components for a certain volume fraction of filler in the composite. Part A (liquid polymer) is first mixed with filler particles in a container. To assure a uniform mixing, stirring of liquid polymer and gradual pouring of filler particles is done simultaneously. Once the uniform mixing of liquid polymer and filler particles is achieved, the hardener (Part B) will be poured into the mixture of liquid polymer and filler, and stirred properly for some time to attain the particle reinforced mould material. Before pouring the mould material into mould box, release agent is sprayed thoroughly inside the mould box. In the box, the (liquid) mixture of Al particle reinforced PU is poured all around the pattern. After that, the box with composite mould material is placed inside the vacuum casting machine to eliminate any traces of entrapped air in the mould, later it is allowed to cure in room temperature. Gradually, it sets with time and becomes a solid rubbery mass with the pattern inside. Now the mould box is cut along a suitable parting line and the RP pattern is removed from within the mould box. Two thermocouple wires are placed on the upper part of the mould box for measuring the temperatures. Then, both the parts of mould box are assembled in the proper position with the help of adhesive tape (as shown in Fig. 2). Once the mould is prepared, liquid wax is poured into the mould and cooling/solidification of liquid wax is done in room temperature.

**Experimental setup**

Once the liquid wax solidifies, both the parts of mould box are disassembled by removing the adhesive tape and the wax component is taken out. After cleaning the mould box, it becomes ready for another casting. It was noticed that the surface of wax component solidifies faster than the core (inside) of the component. Depending on the size/shape of component, a certain depth of solidification from the surface may be sufficient so that the wax component can be taken out from the mould box without any damage. Many times, industrial people follow such technique for shortening the processing time to increase the productivity. Thus, in this experimental study, the measurements of temperature are taken at two distinct positions of the wax component, at the centre and at a depth of 5 mm from the surface of the component. Measurement of temperatures is taken through the thermocouple system (as shown in Fig. 2). The readings of temperatures are collected in an interval of 1 sec through data acquisition system.

**Results and discussions**

The behaviours of cooling rate of the cubical shaped wax component where the mould wall thickness is kept as 30 mm and the outside temperature of mould box is the ambient condition (25ºC) are demonstrated here. The variation of temperatures with time at the location of 5 mm deep from the surface and the core of wax component using PU mould material are plotted in Fig. 3. In Fig. 4, variations of temperatures at the same positions of wax component using Al particle reinforced PU mould material are shown. In both Fig. 3 and Fig. 4, it is noticed that, initially, cooling rate near to surface of component is much faster than that at the core. This is because heat near the surface of wax pattern dissipated only through the mould wall. Whereas heat at the core of wax pattern flows through the mould wall as well as (solidified) wax and the thermal conductivity of wax is quite lower than the mould material. After a long time, both the temperatures gradually come to the atmospheric one. The temperature of liquid wax during pouring in both the moulds made of PU and Al particle reinforced PU was kept almost the same as 85ºC. Figure 3 demonstrates that to reach the temperature, for instance 40ºC at a depth of 5 mm from the surface of wax component, it takes around 80 min in case of PU mould, whereas only 25 min is required in case of particle reinforced PU. Thus, it is revealed that the cooling time is reduced significantly in soft tooling process using particle-reinforcement with mould materials. This happens due to the increase of effective thermal conductivity of mould material. However, besides the thermal conductivity of mould material, the cooling time also depends on the temperature difference between the inside and outside of the mould box, and thickness of the mould wall.

The minimum thickness of mould box is decided based on the shape and size of the wax component to be manufactured. On the other hand, cooling/solidification of wax carried out in ambient temperature is the most desirable technique in industry due to no additional expenditure. Therefore, the only controllable parameter in ST process is the thermal conductivity of mould material which practitioners can improve in order to solidify the wax component with a minimum time.

However, it has been found that though the cooling time is significantly reduced by conductive filler reinforcement with mould material, the stiffness of mould is becoming high. This is happening due to the increase of modulus of elasticity of mould material as a result of particle reinforcement. High stiffness of mould is not desirable in soft tooling process because releasing pattern and wax component from the mould box becomes difficult. Moreover, the values of effective thermal conductivity and modulus of elasticity of a particle reinforced polymeric mould material depend on the type of filler material. By realizing it, in the following section, an extensive experimentation is carried out to find the effect on equivalent thermal conductivity and modulus of elasticity of polyurethane composites due to reinforcement of filler particles, namely, aluminium and graphite with different loading conditions. The existing models of equivalent thermal conductivity and modulus of elasticity of composites are also tried to validate based on the experimental findings which will be helpful to decide the optimum amount of filler content to be reinforced with mould material.

**Equivalent Thermal Properties of Particle-Reinforced PU Mould Materials**

**Experimental measurements: Procedures**

Thermal properties of different composites are measured based on transient plane heat source (TPS) hot disk method (Gustafsson, 1991) following the standard ISO 22007-2: 2008(E). We have used the instrument TPS 2500 S Thermal Conductivity System associated with the software HotDisk Thermal Constant Analyser V.5.9.5 (solids, liquids, powders and paste). The TPS 2500 S Thermal Conductivity System utilizes a hot disk sensor in the shape of a double spiral of nickel wire. The hot disk sensor (design number: C5501) with 14 concentric rings is used here for measuring thermal properties. The sensor element is made of 10 µm thick nickel wire and the spiral is supported by 30 µm thick Kapton material to protect its particular shape by providing mechanical strength and also keeping it electrically insulated. The relaxation time of the probe is less than 10 ms, and the required time to reach a constant temperature difference is kept as 15 min. The sensor used in the experiments has a diameter of 2*a* (*a* is the radius of the largest ring, 6.403 mm) and total thickness (Kapton-nickel-Kapton) of 2*v* (=70 µm) and was placed between two samples of 50 mm square and thickness 5-6 mm. The probing depth of the sensor used for all the samples is around 6 mm. In hot disk method, measurements of thermal properties are made based on the average temperature increase in hot disk sensor. In the following, derivation of average temperature increase in hot disk sensor and the method of computing thermal properties are made.

The differential equation of heat conduction in an isotropic material whose thermal conductivity is independent of temperature is given by (Carslaw and Jaeger, 2000)

where *α* (=*k*/ρ*c*) is the thermal diffusivity, *k* is the thermal conductivity, ρ and c are the density and specific heat of material, respectively. ρ*c* is called volumetric specific heat of the material. *T ***(***x, y, z, t***)** is the temperature at point (*x, y, z*) and time, *t. Q* **(***x, y, z, t***)** (J/m^{3}-s) is the amount of heat released at (*x, y, z, t*) per unit volume and unit time.

The fundamental solution of Eq. (1), assuming that heat source switched at time *t* = 0, is

In cylindrical coordinates, any position in the sample is = (*r*, *θ*, *θ*), any position in the source is = (*r'*, *θ**'*, *z'*) and ( - )^{2} = *r*^{2} + *r'*^{2} - 2*rr'* cos (*θ* - *θ**'*) + (*z* - *z'*)^{2}.

For continuous single ring source with radius a in the z*'* = 0 plane, the heat source strength can be expressed as

in which *δ*( ) is the Dirac delta function (where *f* (*x*)*δ*(*x* - *p*) = *f*(*p*)) and *u*(*t'*) (where *u*(*t'*) = 0 for* t' *< 0 and *u*(*t'*) = 1 for *t'* __>__ 0) is the Heaviside unit step function. *Q*_{0} is the heat released per unit length of ring source.

A hot disk sensor is considered to have m number concentric rings of heat source that are equally spaced (Gustafsson, 1991). Assuming the source is continuous and it is switched on at *t' *= 0, the strength of heat source can be defined as

where *a* is the radius of the largest ring and that of the smallest ring is , and the total length (heating filament) ring (L) is (i.e., (*m* + 1)∏ *a*). Thus, the total heat released by the sensor in time *t* is obtained as

where *P _{0}* is the power output of the hot disk sensor per unit time. Now, the temperature increase caused by hot disk sensor can be obtained by carrying out the integration in Eq. (2) and with the help of Eq. (4):

where *I*_{0} (*x*) = e *e ^{x cos}*

^{θ}*d*

*θ*= e

^{x sin}

^{θ}*d*

*θ*is the first kind modified Bessel function of the 0

^{th}order.

In a hot disk measurement, as the temperature change near the surface of the sensor is concerned, *z* → 0, and by considering the power output of the hot disk sensor per unit time (*P _{0}*) instead of

*Q*, Eq. (7) may be written as

_{0}Equation (8) may be rewritten by introducing some new parameters as follows

where σ is an integration variable defined as and the (dimensionless) parameter, τ is called the characteristic time ratio.

Thus the temperature increase at any point on the sensor surface (i.e., *z*-plane) is described by the Eq. (9). But to determine the temperature increase of the sensor itself, it is required to determine the average temperature increase over the length of the concentric rings. Therefore, the average temperature increase of the sensor is defined as

By replacing the expressions of *Δ**T*(r,τ) (from Eq. (9)) and *L* (as cited above) in Eq. (10), *Δ*(τ) may be expressed as

where *k* is thermal conductivity of materials. D(τ) is a dimensionless time function.

From Eq. (11), it can be seen that average temperature increase in hot disk sensor, *Δ*(τ) is linearly proportional to the dimensionless time function, *D*(τ) and exhibit straight-line curve by plotting their values. The slope of this straight-line curve is equal to from which the value of k may be evaluated. But the straight line curve between *Δ*(τ) and *D*(τ) may be obtained for a proper value of τ that is again dependent on the value of *α* (for a given value of *a* and time *t*). Therefore, it is required to find the proper value of α and, normally, this may be done by making a series of computational plots of *Δ*(τ) versus *D*(τ) for a range of *α* values. The correct value of α will be reached once the straight-line plot of *Δ*(τ) versus *D*(τ) is obtained. Once the correct value of *α* is obtained, the value of *k* can be determined from the slope of the straight-line plot of *Δ*(τ) versus *D*(τ).

Another way to determine the value of *k* is to measure the density (*ρ*) and the specific heat (*c*) of the material separately. Then, the value of *k* can be obtained by multiplying the value of *k* by the density and specific heat of the material. This method is generally applied for anisotropic materials. If the properties along *x*- and *y*- axes are the same, but different from those along the *z*-axis and if the plane of the hot disk sensor is mapped out by *x*- and *y*- axes, Eq. (11) will be expressed as

where *k _{x}* and

*k*are the thermal conductivities in the

_{z}*x*(or

*y*) and

*z*directions respectively and = . The value of

*k*can be determined by the above stated iteration process until a straight-line plot of

_{x}*Δ*() versus

*D*() is reached and the value

*k*is equivalent to

_{x}*αρ*

*c*. On the other hand, from the slope of the straight-line plot of

*Δ*() versus

*D*(), the value of can be found out. Therefore, the value of

*k*is calculated by dividing the value of by obtained value of

_{z}*k*.

_{x}**Composite sample preparation**

The same procedure as described in "Preparation of mould and manufacturing of wax component" subsection is adopted here to prepare the composite samples for thermal property measurements. As per the standard, ISO 22007-2: 2008(E), the composite samples are made in the size of 50 mm square and thickness is kept as 5-6 mm.

**Experimental results and discussions**

The equivalent thermal conductivity (ETC), thermal diffusivities and volumetric heat capacity of particulate filled PU composites with Al and graphite particles for different amount of filling fractions as obtained through experimentations at room temperature (23ºC) are illustrated in Fig. 5. From the experimental results, it is quite evident that thermal conductivities of particulate filled PU and SR are increasing (around 10 times) with increasing amount of filler and the increasing rate starts more drastically at around 20-30% volume fraction of filler for some composites. This is due to the formation of thermal conductive chain in composite whose tendency is high in elevated filler content. In Fig. 5, another point noticed is that increasing rate of thermal conductivity is comparatively higher for any level of filler content when graphite filler is used for both the mould materials. The reason is: large particles which are equivalent as the composed of aggregates of filler particles are more capable of forming conductive chains than fine particles. Moreover, the amount of heat scattered around the contact points in case of coarse particles is smaller than in fine particles, since less number of contact points are required to form the same length of conductive chain (Agari and Uno, 1985).

On the other hand, it is worth mentioning that manufacturing process of composite is an important aspect to achieve a maximum value of ETC of flexible mould material composites. Because there is more possibility of the presence of voids in mould due to fault(s) in manufacturing, which will reduce effective thermal conductivity. This phenomenon is observed in the results of PU-Al composites (Fig. 5(a)). It is found that though the composite contains higher filler (48.66%), it exhibits lower ETC than that having lower (39.922%) filler due to presence of more voids (as seen in Fig. 6).

**Validation of Existing Models Based on Experimental Results**

The experimental results of ETC of the composites have been explained by several empirical/semi-empirical models, namely Maxwell-Eucken (Maxwell, 1954), Bruggeman (Bruggeman, 1935), Lewis-Nielsen (Lewis and Nielsen, 1970), Cheng-Vackon (Cheng and Vachon, 1969), Ziebland (Butta and Migliaresi, 1996), Torquato (Torquato, 1985) and Agari-Uno (Agari and Uno, 1986), as shown in Fig. 7. It is observed that Lewis-Nielsen model (which is defined by empirical expression as shown in Eq. (13)) provides closer estimations (average % error = 29.21) than other empirical models in all four composites.

where and

*k _{c}*,

*k*, and

_{p}*k*represent the equivalent thermal conductivities of composite, polymer, and filler, respectively, and

_{f}*V*is the volumetric fraction of filler in the composite. The constant A depends on the shape and orientation of disperse particles in the composite, and is defined by

_{f}*A*= - 1 (where

*k*is the Einstein coefficient). φm is the maximum packing fraction of disperse phase (for randomly distributed spherical particles,

_{E}*φ*

_{m}= 0.637). The value of A is equal to 1.5 for randomly distributed spherical particles, while in case of randomly distributed aggregates of spherical particles,

*A*= 3.

Moreover, a better fit is observed with the semi-empirical model of Agari-Uno (expressed by Eq. (14)) whose controlling parameters are determined based on the experimental data. The average % errors of Agari-Uno model are found as 2.35 and 10.12 by individually fitting the composite systems of PU-Al and PU-Graphite, respectively. However, it was found that the average % error of Agari-Uno model by fitting all the data of two composite systems is considerably high (16.95%), though still lower than Lewis-Nielsen model.

where *C _{1}*, the factor of the effect on crystallinity and crystal size of polymer, does not depend on particle size.

*C*is the factor of ease in forming conductive chains of particles, which is affected by filler particle size.

_{2}In looking at the Agari-Uno models, it was found that values of *C _{1}* (0.933594 and 1.0) are nearer/equal to 1.0 and the values

*C*are 0.625 and 0.852295 for the suspension systems, PU-Al and PU-graphite, respectively. Value of

_{2}*C*close to 1.0 indicates that effect of crystallinity and crystal size of polymer on the changing thermal conductivity of polymer (matrix material) is negligible due to the inclusion of filler. Such kind of effect is observed in flexible mould material composites with both the graphite and Al particles. The value of

_{1}*C*close to 1.0 indicates more ease in forming conductive chains of filler particles in composite. In the present composites, it is observed that the value of

_{2}*C*is greater for large particle size filler (graphite) than the smaller one (Al) which agrees well with the results of Boudenne et al. (2004).

_{2}

**Equivalent Modulus of Elasticity of Particle-Reinforced PU Mould Materials**

**Experimental measurements: Procedures**

Modulus of elasticity of a material may be tested using different standard test methods, namely tensile testing, four-point loading test (Gere, 1984), ultrasonic measurement (Moore, 2007), etc. The tensile testing method we have adopted here to find the equivalent Young's modulus of flexible mould material composites is based on the standard ASTM D 3039M-08. According to this standard, a constant rectangular cross-section shaped specimen of thickness, 2.5 mm ±4%, 25 mm ±1% of width and 270 mm of length in the form of sheet is prepared using the method as described in "Preparation of mould and manufacturing of wax component". Tensile tests are performed on an Instron testing machine (made of DARTEC). The testing machine is equipped with a recording system (load sensor) for measuring the applied force within ±2% and is capable of measuring elongation of the test specimen in minimum increments of 10%. The machine has two grips, one of which is connected to the load sensor. The grips (constant pneumatic and wedged type) are tighten automatically and exert a uniform pressure (of maximum 10 bar) across the gripping surfaces which is increasing as the tension increases in order to prevent slippage and to favour failure of the specimen in the straight middle section. At the end of each grip, a positioning device is placed in order to insert specimen to the same depth in the grip and to make the specimen aligned with the direction of pull. An extensometer (Made of MTS, Model No. 634.25F-24, Serial No. 10288577A) is used to measure the strain of test specimen. The extensometer was calibrated by M/s MTS. The extensometer was attached to the specimen at two points of 50 mm apart (extensometer gauge length) symmetrically about the mid-span and mid-width location. During experimentation, a value of constant head-speed of 5 mm/min is applied and the force applied to the specimen until a maximum value of elongation, 15% or failure of the specimen whichever is occurred earlier. The values of displacement, force and strain are recorded through data acquisition system at a constant interval of 0.01 sec. After plotting the data of stress vs. strain, a linear curve is found which indicates the elastic region of the stress-strain diagram of the material. The slope of this linear curve is evaluated, which represents the tensile modulus of elasticity of composite moulds.

**Experimental results and discussions**

From the experimental results as illustrated in Fig. 8, increase of modulus of elasticity is observed in all kinds of flexible mould materials reinforced with conductive filler particles. In PU composite system, increase of modulus of elasticity is more-or-less similar in nature for both the reinforcements, Al and Graphite, especially when the filler concentration label is below 40%. But a sudden rise of modulus of elasticity is observed with Al filler at above 40% volume fraction, unlikely to that filled with graphite particles. This may be due to the fact that Al particles are securely embedded with polymer matrix since the size of particles is comparatively smaller than graphite particles. This phenomenon is specifically observed when the filler content is more than 40%. Whereas, adhesion between PU and graphite particles is not as critical as compared to polymer matrix and metallic filler composite systems. The effective modulus of elasticity of particle filled flexible (polymeric) mould material composite also depends on the modulus of elasticity of the polymer, modulus of elasticity of filler material, and the volume/weight fraction of filler particle in the composite.

**Validation of existing models based on experimental results**

The experimental results of equivalent modulus of elasticity of the particulate filled polyurethane and silicone rubber composites, as illustrated in Fig. 8, are explained using various existing empirical models available in the literature. The most commonly used models for predicting equivalent modulus of elasticity of a composite material in a straightforward way, from its numerical expressions are the following:

**Model proposed by Paul** (Paul, 1960):

where *E _{m}*,

*E*and

_{f}*E*are the modulus of elasticity of the matrix, particle and composite, respectively.

_{c}**Model proposed by Ravichandran** (Ravichandran, 1994):

where

**Model proposed by Wu** (Wu, 1965):

where *V _{m}* (= 1-

*V*) is volume fraction of matrix material.

_{f}*λ*is the parameter, which remains fixed for any relative concentration of a given composite material. Through experimental study, it has been found that the value of

*λ*is quite close to unity for << 1.

Besides the above models, there are many empirical expressions proposed by various researchers, namely Hashin-Shtrikman bounds (Hashin and Shtrikman, 1963), Halpin-Tsai models (Halpin, 1969; Halpin and Kardos, 1976), Walpole bounds (Walpole, 1966a; Walpole, 1966b), methods based on mean-filed (such as Voigt model (Voigt, 1889), Reuss model (Reuss, 1929), Mori-Tanaka*'*s models (Benveniste, 1987), etc.), self-consistent method based models (Kroner, 1958), models based on differential method (McLaughlin, 1977), Lielens models (Lielens et al., 1998) from which the equivalent modulus of elasticity (or its upper bound (UB) & lower bound (LB)) of a particulate filled composite can be determined based on the conventional expressions (Eq. (19)) of isotropic material properties by assuming the composite to be (quasi) isotropic and (quasi) homogeneous.

where *E*, *G* and *K* are the modulus of elasticity, shear modulus and bulk modulus, respectively.

If the Lielens model is formulated based on a normalization of the upper and lower bounds suggested by Hashim-Shtrikman, it can be written as

where *f* = , and , , and are the Hashin-Shtrikman lower and upper bounds of bulk modulus and shear modulus, respectively, which are expressed by the following empirical expressions:

In Fig. 9, the equivalent modulus of elasticity of particle reinforced PU composites obtained using various models are illustrated. Through rigorous comparative study among the experimental results with that obtained from various models, it is found that the model proposed by Lielens, with normalization of the upper and lower bounds suggested by Hashim-Shtrikman (defined in Eq. (20) and Eq. (21)), provides close agreements with experimental data compare to other models, particularly up to a volume fraction of 0.3 of the particulates. From Fig. 9(i) to Fig. 9(ii), it has been observed that most of the experimental data of all the suspension systems lie in the region enclosed by the Hashim-Shtrikman upper and lower bounds. The model seems to be efficient enough to predict the modulus of elasticity of the PU composites with varying matrix as well as reinforcement particles.

**Conclusions**

In the present work, an experimental study is carried out to find the equivalent thermal properties and effective modulus of elasticity of particle reinforced PU mould material using hot disk technique and tensile testing method, respectively. The measurements of thermal properties using hot disk technique and modulus of elasticity using tensile testing method are presented. A significant increase of thermal conductivity as well as modulus of elasticity of PU composite mould material (reinforced with Al and graphite particulate fillers) is observed. As a result, it has been found that the cooling time in soft tooling process is much reduced, but simultaneously increase of stiffness of mould box is observed. Therefore, determination of an optimum amount of filler content with mould material is important. Presence of voids in the composite due to manufacturing fault(s) reduces the effective thermal conductivity considerably. By comparing the experimental results of equivalent thermal conductivity of PU composites with the existing models, it is observed that data driven model by Agari-Uno and numerical model by Lewis-Nielsen provide better estimations than other models. On the other hand, model proposed by Lielens shows better trade-off with experimental findings of equivalent modulus of elasticity of particle reinforced PU compared to other models.

**Acknowledgements**

The authors are thankful to DST (Department of Science and Technology), New Delhi, India, for supporting this research work under the BOYSCAST fellowship programme.

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Paper received 11 May 2010.

Paper accepted 22 October 2010.

**Technical Editor: Anselmo Diniz**