Review Article | Open Access
Evan Mitsoulis, "50 Years of the K-BKZ Constitutive Relation for Polymers", International Scholarly Research Notices, vol. 2013, Article ID 952379, 22 pages, 2013. https://doi.org/10.1155/2013/952379
50 Years of the K-BKZ Constitutive Relation for Polymers
The K-BKZ constitutive model is now 50 years old. The paper reviews the connections of the model and its variants with continuum mechanics and experiment, presenting an up-to-date recap of research and major findings in the open literature. In the Introduction a historical perspective is given on developments in the last 50 years of the K-BKZ model. Then a section follows on mathematical modeling of polymer flows, including governing equations of flow, rheological constitutive equations (with emphasis on viscoelastic integral constitutive equations of the K-BKZ type), dimensionless numbers, and boundary conditions. The Method of Solution section reviews the major developments of techniques necessary for particle tracking and calculation of the integrals for the viscoelastic stresses in flow problems. Finally, selected examples are given of successful application of the K-BKZ model in polymer flows relevant to rheology.
Rheology is defined as the “study of deformation and flow of matter” [1, 2]. The term has ancient Greek roots that refer back to the 6th BC, when the Greek philosopher Heraclitus realized the relative change of all elements in his well-known motto “” or “everything flows” . In our days the term “rheology” was first used in 1920 by the American chemistry professor Eugene Bingham in Lafayette College, Indiana, USA. Bingham consulted with colleagues in the Department of Classical Studies in his effort to explain the peculiar behavior of various colloidal solutions . The term “rheology” and its above definition were accepted by the (American) Society of Rheology (SOR), founded in 1929 with its first president being Prof. Bingham. Many other national rheological societies have since come to being, with the European Society of Rheology (ESR) established in 1996 and encompassing many individual European societies. The various rheology societies celebrate every four years the advancements in rheology at the International Congress on Rheology. The last one took place in Lisbon, Portugal, in August 2012 .
According to the Heraclitian definition, the term “rheology” could be used for all materials, including the classical limit cases of Newtonian fluids, such as water, and elastic Hookean solids, such as metals. However, these limiting cases are often considered outside the scope of rheology, which deals mainly with materials characterized by complex behavior. As an example, the 1st annual meeting of SOR in 1929 in the USA included presentations on asphalt, lubricants, paint, plastics, and rubber, which gives an idea of the broad scope of the subject matter and the various scientific disciplines implicated in rheology. Today the subject of rheology has seen tremendous growth and includes polymer rheology (plastics and rubber), colloidal rheology, suspension rheology, biorheology, food rheology, and so forth .
Since rheology deals with flow and deformation, it has been customary to take as predominant the term “flow” (to flow means “” or “rheo” in ancient Greek) and study the flow (and deformation) of complex fluids, which are then called “non-Newtonian” fluids. The Journal of Non-Newtonian Fluid Mechanics (JNNFM) was established in 1976 and has been published ever since uninterruptedly by Elsevier .
Most non-Newtonian fluids under study in rheology exhibit highly nonlinear behavior under flow and deformation. This nonlinearity is known for polymeric materials as shear thinning (or pseudoplasticity) and governs the viscosity as a function of the shear rate. Other materials exhibit time-dependent phenomena of shear thinning and are called thixotropic. The presence of macromolecules in polymers is responsible for elastic phenomena, and this gives rise to viscoelasticity, which includes the relaxation time of the material.
When time of response of the materials comes into play, the traditional idea of solids and fluids may no longer be valid, and a different classification need be applied. This is taken into account when considering the rheological behavior of the materials, and the classification is more appropriate according to the rheology of the materials. The time constant present in the rheology of time-dependent materials gives rise to the dimensionless Deborah number (De). When , the material behaves as a Newtonian liquid, while when , the material behaves as a solid. In-between values of De describe most of real materials.
Since rheology deals with the flow and deformation of matter in the most general case of time-dependent and three-dimensional space, it is necessary to describe such behavior by introducing differential calculus with tensor and vector notation in time and space. This makes the subject rather difficult and needs a good grasp of mathematics and physics. Some simple cases (usually one-dimensional) have analytical solutions. However, most cases require numerical solution, and this leads to the need for a good knowledge and experience with numerical analysis and computational methods. The presence of powerful computers and workstations has allowed the solution of many important problems in rheology. Still many more remain unsolved and are the subject matter of intensive research efforts.
The main current subjects of rheology deal (i) with rheometry (experimental methods for measuring the rheological properties of the materials), (ii) with constitutive equations (mathematical models for describing the rheology of the materials), and (iii) with complex flows (for visualizing and understanding the flow behavior of materials).
A major part of rheological research relates to polymers. Since the tremendous growth of the plastics industry, especially after the 2nd World War, it was realized that the making of plastic products involves the flow and deformation (hence rheology) of macromolecules (polymers). These were found to behave as highly non-linear non-Newtonian fluids, producing flow phenomena in sharp contrast to Newtonian fluids. The rheological community was then hard pressed (i) to find ways to measure the properties of these materials (hence rheometry), (ii) to model them with appropriate rheological models, and (iii) to predict their flow behavior in industrial operations, collectively known as “polymer processing.” This proved to be a daunting task, and many researchers around the world have contributed to a level of sophistication in all three areas above commensurate with the industrial importance of the subject.
An intellectually challenging endeavor was to formulate rheological equations of state (constitutive equations) able to describe well the unusual behavior of macromolecules (polymers). Many efforts were initiated, mainly at universities, and a plethora of constitutive equations saw the light with varying degrees of success. The present work refers to one such example of constitutive equations that saw the light 50 years ago (in 1962) and has since captured the imagination and research efforts of various scientific groups around the world. This is the K-BKZ integral constitutive equation [7, 8], which, arguably, has shown most promise in mimicking and predicting the behavior of polymer solutions and melts in flows of scientific and industrial importance. The present paper draws heavily on Tanner’s work  which celebrated the 25th Silver Jubilee of the K-BKZ model. It brings up-to-date information and more examples of the successful application of the K-BKZ model to polymer flows to help celebrate the 50th Golden Jubilee of this remarkable model.
1.2. The K-BKZ Original Papers
In 1963 the Transactions of the Society of Rheology (now Journal of Rheology) published the article known from the initials of its authors as the BKZ paper  (see Figure 1 regarding the three authors ). The article was presented to the Society of Rheology (SOR) at its annual meeting in October 1962; Alan Kaye’s note  expounding essentially the same ideas shares this date. Tanner in his review paper , celebrating 25 years of the model, charts the citations of these two articles from its birth. He depicted data taken from the Science Citation Index, covering the period 1963–April 1987. The two papers were closely linked and the rates of total citations were roughly in the proportion 140 (BKZ) to 50 (Kaye), each author seeming to attract about a quarter of the attention, which appears a fair result.
These numbers have now been extended to the present date covering 50 years of the model. Taken from the same source (Science Citation Index, ISI) , the data up to 2012 give 501 citations for BKZ and 150 for Kaye, keeping roughly the 1/4 ratio for each author. The search for “BKZ” mentioned in an article brings out about 2000 papers (without self-citations by the authors) as shown in Figure 2. By all means the BKZ paper remains a citation classic, a status enjoyed by a mere fraction of published papers (in the rarefied world of 0.002%) .
The pattern of citation is also quite abnormal. Generally, most citations occur within five or so years of publication and thereafter papers are quietly forgotten. Following the results presented by Tanner , the BKZ model got more attention in 2010 alone (220 citations) than in any other year since its presentation 50 years ago. Obviously, there must be good reasons for this, and in this paper more evidence will be given for the model’s use and its successes.
2. The K-BKZ Constitutive Model
From the inception of the basic ideas of a mathematical model to make it suitable for engineering applications, a long and arduous way has to be followed, along which a number of key people have contributed to make this happen. The following constitutes in the simplest possible terms a guide along that pathway that led from the original ideas to the current use of the model and its variants in engineering applications.
2.1. One-Dimensional Model
Before describing the general theory let us consider the one-dimensional (1D) shearing case, following Tanner . Application of a step shear strain of magnitude to an unstressed sample at time will result in a shear stress response ; if the response is linear in we can write  where is the relaxation modulus and is the time interval. Application of a series of steps at various times results in the linear response and in the limit of a continuous strain history
We can integrate (3) by parts to find where and . The function is usually referred to as a memory function as it depends on the time interval . If we now measure from the present configuration as reference, as is convenient in fluids, then (4) becomes One can look at (5) as a superposition of linear, noninterfering effects as before, known also as Boltzmann’s superposition principle. If we now permit to depend on the strain level, becoming a noninterfering superposition of nonlinear responses, then or letting where then (5) becomes which is the one-dimensional K-BKZ model.
2.2. Three-Dimensional Model
In the fully three-dimensional (3-D) case, for an incompressible fluid, the equation as developed in the original BKZ article  reads where is the total stress tensor, is the pressure, and is the unit tensor. The notation for meant
The notation introduced in (10) is not simple, and further useful definitions are required to make it easier to understand. Figure 3 shows a relevant notation of the position vector , velocity vector , and times (present) and (past).
The right Cauchy-Green strain tensor is defined as and the strain tensor is defined as
In (10) is a “potential function” and is assumed to be a function of and ). Furthermore, for the isotropic fluids considered here, is a function of the invariants and of , where and is the strain tensor defined in (13). The third invariant of () need not be an argument of for incompressible materials (being 1).
In (11) and (12) one notes the dependence of the strains on the coordinates at two times, and . We shall use the present () coordinates as a reference frame and write the equivalent of (11) as (Cartesian tensor notation, ) where () is the relative deformation gradient tensor. With this definition the tensor is equivalent to or the inverse of the Cauchy-Green tensor relative to the coordinates as reference. We shall refer to this strain as the Finger strain tensor, .
The tensor is then just . With these changes of notation, (10) becomes
This is the form of the original BKZ equation .
2.3. Kaye’s Contribution
Kaye  went straight for a generalization of the rubber-like liquid of Lodge . With the notation used above, he wrote, for the rubber-like liquid, where is another memory function; he recognized that this is related to the simplest form of the theory of rubber elasticity  where is defined in (12). The simplest function is where is constant. In this case
Equation (20) translates into (17) for a rubber-like liquid. The most general incompressible rubber-elastic theory [13, 14] was known by Kaye  to give (here is measured relative to the undeformed configuration), where the corresponding rubber-elastic liquid was given as and , .
Equation (23) appears to be the most convenient form of the constitutive equation . Here we have and , and is a function of , , and . The transformation of the original form of (16) into the form of (23) did not appear in the 1965 BKZ article ; it appeared however in the article by Zapas and Craft  of 1965. Further developments for the nonisothermal case were given in 1964 . Thus from 1965 on, the theory was essentially complete in the form now generally used. We now look at the variants of the model proposed by other researchers in an effort to make it tractable for numerical simulations.
2.4. Other Contributions
Tanner  describes how it is possible to trace the elements of K-BKZ theory in the continuum mechanics literature. It begins from the formulation [18, 19] which gives the stress tensor as a functional of C for a simple fluid over all past times. Pipkin  gives where is another memory function. For reasons beyond the scope of the present work, (24) with as a strain measure does not provide a realistic constitutive equation . A better description is obtained if one substitutes with a function to get Here the memory function is the same as that in (5) provided we scale appropriately; it is also equal to in (17). The general form of is known to be, from rubber elasticity  (to within an isotropic tensor), where , , and and are functions of these invariants. Hence (25) becomes where is evaluated at relative to the reference state at . Choosing a strain measure optimal in some sense in the above equation is an idea with obvious appeal.
One can go further and note that (27) is the separable case (in the sense that the memory function m is independent of the strain measure ) of the more general rule where are functions of , , and . This rule was first given by White and Tokita  and then later by Rivlin and Sawyers . This generic integral model includes many other well-known constitutive equations, whose rheological response is studied in the monographs by Bird et al. , Larson , and Tanner . For example, and , and assuming separability for the memory function yields the Lodge rubber-like liquid model .
The factorized K-BKZ model proposed by White and Tokita  can be written for the extra stress tensor as where there is separability between the time-dependent function and the strain-dependent function .
The Rivlin-Sawyers variant of the K-BKZ model is written as where is not a potential function. Its factorized version is then written as where is a strain-dependent function.
Tanner  argues that, strictly speaking, the above equations are not the K-BKZ equation, and he offers an example of very fast deformations to see the difference. Also, the above equations do not include a potential function , as the original BKZ model. However, as Tanner  continues to conclude, “there seem to be few cases where any problems have arisen with a lack of potential, and many applications proceed using versions of (28), despite the possible dangers that might arise if fast deformations were to be investigated.”
At this point and starting in 1976, there were serious efforts to make the above models tractable to fit rheological experimental data and make them available for simulations. The impetus was given by Meissner’s IUPAC Working Party data on low-density polyethylene (LDPE) published in 1975 . The data was extensive, and a comprehensive set of rheological data for an important industrial polymer at last became available to people in the field.
Wagner  began to describe the IUPAC-LDPE data by K-BKZ forms. Generally he used the equation in the form where was termed the “damping function,” which is a function of and ; these are the traces of and , respectively, and is the time-dependent or memory function.
The memory function can be found from small-strain data according to the linear viscoelastic theory; it is usually given as a sum of exponential functions involving the relaxation times and relaxation moduli for relaxation modes The number of modes depends on the polymer melt, but usually 4–8 modes are enough to capture the linear viscoelastic data , while for polymer solutions less modes (2-3) are enough .
The damping function is not a unique function and many similar functions have been proposed to match experimental data. Wagner  for general flows used where is a fitted parameter. Later, Wagner et al.  used a strain invariant to reconcile shear and elongational data; here is a fitted parameter to be determined from elongational data. Thus, the Wagner model uses
Around 1980 a number of damping functions were available, so that Dan Joseph in his graduate course on Rheology referred to his list of these functions as a “Drugstore of Rheology” . Papanastasiou et al. , having taken Joseph’s course on rheology at the University of Minnesota, proposed the following fractional damping function:
The resulting model has been known in the literature as the Papanastasiou-Scriven-Macosko or K-BKZ/PSM model, and it has been widely used in numerical simulations as will be detailed later. The constants and in the damping function can be obtained independently from shear and elongational data, respectively.
A more complete form of the model was proposed by Luo and Tanner  to account for a nonzero second normal stress difference and for a better fitting of elongational data. The K-BKZ/L-T model is written as where In the above, and are the first and second normal stress differences, respectively. The constant is a negative number and usually in the range of −0.1 to −0.25 . The multiple values correspond to different elongational behavior for each relaxation mode.
The above more tractable integral equations were further rectified. Wagner  introduced the “irreversibility” argument to solve the excessively elastic recoil problem exhibited by the above models. In this model, the damping function becomes “inelastic” or “irreversible” in the following way: when the strain changes between time and , one selects the lowest value of that exists over this time segment. Another rectification was given by Olley , who proposed a modification of the PSM damping function so that different responses could be obtained in uniaxial and in planar extension (note that with the PSM damping function the planar extensional viscosity follows the shear viscosity). The Olley damping function reads and can give independent planar extensional behavior from its shear counterpart without compromising the uniaxial elongational behavior.
Tanner  goes on to relate how the K-BKZ model is also connected with microstructural theories. Under this line of thought the reptation model of Doi and Edwards [34–36] for entangled linear polymers, further extended by Curtiss and Bird , can also be written in the form of (28) using Currie’s  approximation of the related potential function. Then the Doi-Edwards model is given by It contains only two adjustable parameters, namely, the zero-shear-rate viscosity and the time constant .
Integral constitutive equations proposed more recently on the basis of molecular theories for linear and branched polymers have a more complicated mathematical structure (integrodifferential forms) and are beyond the scope of the present paper. The interested reader is directed towards the developments made by Mead et al. , McLeish and Larson , Ianniruberto and Marrucci , Wagner et al. , Hassager et al. , Hassager and Hansen , and so forth.
3. Fitting Experimental Data with the K-BKZ Model
The idea behind any model is to fit well experimental data in an effort to use physics and mathematics to mimic nature. The K-BKZ model and its more tractable variants (such as the PSM model  or the L-T model ) have enough degree of complexity as to guarantee good fit of many experimental data obtained from rheometry. In the following, examples are given of how to use the model to obtain useful fitting of experimental data for two main polymer melts of industrial importance, namely, a low-density polyethylene (LDPE) and a high-density polyethylene (HDPE).
3.1. Data Fitting
In the review article by Tanner  celebrating 25 years of the K-BKZ model, an example was given of how to fit the rheological data for the IUPAC-LDPE melt. It was shown that the time-memory function consisted of relaxation modes, and for each mode there were values of , , and , . The fitting was completed by setting the other two constants, namely, and . It was thus necessary to have constants to fit the rheological data.
One may argue that these are just too many constants to fit. However, and upon closer inspection, this is not such a daunting task. The required relaxation spectrum can be easily obtained from a single experiment of collecting data for the linear viscoelastic storage and loss moduli, and , respectively. These in turn are given as a function of frequency as follows (by assuming a Maxwell model for each mode) : These functions are independent of the strain-memory function (hence separability of the functions or factorized K-KBZ model), and only and can be determined from dynamic data of the viscoelastic moduli. As an example we give in Figure 4 and Table 1 the fitting of experimental and data for an LDPE melt  and an HDPE melt , where it is shown that a spectrum of 8 relaxation times, ranging from s to s, is able to capture well the data at all frequencies. It should be noted that the fitting is not very difficult and can be done even with an MS Excel software, provided that one uses a reasonable number of relaxation times (8 for polymer melts or 3 for polymer solutions) with initial guesses for the relaxation times submultiples or multiples of 10 and appropriate initial guesses for the relaxation moduli [30, 47]. A commercial code IRIS  is also available based on the parsimonious model of Baumgaertel and Winter , which finds the minimum number of relaxation modes to fit the data. Thus, the time-memory function presents no problem in fitting well experimental data for and and finding the related parameters.
The strain-memory or damping function is derived from the first and second invariants of the Finger strain tensor. For simple shear flow, the strain-memory function is given as where is the shear strain. The strain-memory function in simple shear flow is dependent on but not on . This is expected since is viewed as a shear parameter, while is viewed as an elongational parameter. Thus, data on versus can be fitted to give the value of parameter . However, an easier way is to have shear viscosity () data as a function of shear rate, something which is easily available with today’s rheometers. Again, the shear viscosity data is used to find the best value of parameter . This is shown in Figure 5 for the two melts, namely, LDPE and HDPE.
The elongational parameter (or if multiple parameters are needed) is determined from elongational data, either steady state or transient. In the earlier days of the 1960s and 1970s, elongational viscosity data were very hard to come by, and Meissner and his group  were virtually the only ones to produce reliable data on elongational viscosity. This situation has now been much improved because of two important developments, the filament-stretching device of Sridhar and McKinley [50, 51], and the Sentmanat Elongational Rheometer (SER) . Thus, fitting elongational data obtained by these devices, the parameter of the model is readily obtained, as shown in Figure 6 for the LDPE and HDPE melts. The value of is usually set to be a small negative number (around −0.1) according to experimental evidence .
With the determination of the fitting parameters, it is thus possible to obtain a good fit for steady-state rheometric functions, such as the shear viscosity, , first normal stress difference, , and uniaxial elongational viscosity, . Then the other extensional viscosities in planar extension, , and in biaxial extension, , are predicted by the model. These predictions can also be extended to transient effects for all rheological functions at different times [30, 47].
4. Mathematical Modeling
4.1. Governing Conservation Equations
In order to study polymer flows in rheology and inside processing equipment, it is essential to consider first the governing flow equations. The flow of incompressible fluids (such as polymer solutions and melts, at least in situations where they are considered as incompressible for pressures below 100 MPa) is governed by the usual conservation equations of mass, momentum, and energy [1, 23], that is, where is the velocity vector, is the scalar pressure, is the extra stress tensor, is the density, is the heat capacity, is the thermal conductivity, and is the temperature.
The above system of conservation equations is usually called the nonisothermal Cauchy or momentum equations in Fluid Mechanics.
4.2. Constitutive Equations
The above system of conservation equations is not closed for non-Newtonian fluids, such as polymeric liquids, due to the presence of the stress tensor . The required relationship between the stress tensor and the kinematics (velocities and velocity gradients) must be given by appropriate rheological constitutive equations, and this is an eminent subject in theoretical rheology as explained in Section 1.1 [1, 23, 24]. To address this issue all the aforementioned efforts in developing the K-BKZ model were directed.
However, it is always instructive to consider the simplest possible models for purely viscous fluids, so that the differences due to viscoelasticity with the K-BKZ model become apparent. The simplest viscous rheological constitutive equation that relates the stresses to the velocity gradients is the generalized Newtonian model [1, 23] and is written as where is the rate-of-strain tensor and is the apparent viscosity given in its simplest form by the power-law model [1, 23] where is the consistency index and is the power-law index (usually , representing a degree of shear thinning). Other popular models for viscosity computations—among others—are the Carreau model  given by and the Cross model  given by In the above, is the zero-shear-rate viscosity, is the infinite-shear-rate viscosity, is a characteristic time, and is the power-law index. The magnitude of the rate-of-strain tensor is given by where is the second invariant of the rate-of-strain tensor. The Carreau model describes well the shear thinning behaviour of polymer solutions and melts for all shear rates and exhibits two plateaus for low and for high shear rates, while for intermediate to large shear rates it represents well the power law.
The effect of temperature on the viscosity is of primordial importance in polymer processing flows, where tight control of temperatures is required for a successful operation. The viscosity as a function of temperature is given by an exponential relationship, according to [1, 23, 53] where is a temperature-shift factor in the expression that relates viscosity to temperature, and is the viscosity at a reference temperature, . The values of for polymers are usually in the range of 0.01–0.04/C but occasionally they may reach 0.1/C or more for some polymers.
Another expression for the temperature dependence of the viscosity is the Arrhenius law [1, 23, 53]: where is the ideal-gas constant (=8.13 J/Kmol), is the activation energy for flow (J/mol), is the absolute temperature (K), and is the absolute reference temperature (K).
For the integral K-BKZ model and its variants, the nonisothermal version comes about from applying the time-temperature superposition principle . This simply consists of shifting the relaxation times from the temperature history within the material’s internal time scale . The equation used to shift the relaxation times in the material’s history is given by [54–56] where is the temperature at time . The viscoelastic stresses calculated by the nonisothermal version of the K-BKZ model enter in the energy equation (see (46)) as a contribution to the viscous dissipation term.
Similarly with the time-temperature superposition principle where the stresses are calculated at a different temperature using the shift factor , the time-pressure superposition principle can be used to account for the pressure effect on the viscosity and hence the stresses. In both cases of viscous or viscoelastic models, the new stresses are calculated using the pressure-shift factor defined by the Barus equation [57, 58] where is the viscosity at absolute pressure , is the viscosity at ambient pressure, and is the pressure coefficient.
For viscous models, (57) is used to modify the viscosity. For viscoelastic models, such as the K-BKZ model, the pressure-shift factor modifies the relaxation moduli, , according to This is equivalent to multiplying the viscoelastic stresses by .
4.3. Dimensionless Groups
Before proceeding with the boundary conditions, it is important to examine the relevant dimensionless numbers in polymer flows through dies used in rheometry and in processing equipment. The dimensionless groups are calculated at a reference temperature, here taken as the temperature of the process, . As a characteristic length it is usually assumed the smallest dimension, for example, in a capillary tube its radius, . As a characteristic speed it is usually assumed the average velocity defined by using the volumetric flow rate according to
A characteristic apparent shear rate is then defined according to and a characteristic viscosity is given as a function of apparent shear rate and reference temperature, that is, For a power-law model, the characteristic viscosity can be found as where the material parameters and are calculated at .
The relative importance of inertia forces in the equation of momentum is assessed by the Reynolds number, defined for Newtonian fluids by where is the characteristic diameter (=). It is noted that for most polymer melt flows the Re number is usually small, in the range of 0.0001 to 0.01. Therefore these flows are inertialess or creeping.
For viscoelastic fluids with a relaxation time , several dimensionless groups can be defined, but these can be seen as being equivalent . For example, the Deborah number (De) is defined as where is a material relaxation time, is a process relaxation time usually taken to be equal to 1/, and is a shear rate usually evaluated at the channel wall. The Weissenberg number (Wi, also written as We or Ws) is defined as The recoverable shear or stress ratio () is defined as where is the first normal stress difference and is the shear stress, both evaluated at the channel wall. The equivalence is evident when we take where is the first normal stress difference coefficient and is the shear viscosity. The case of corresponds to inelastic fluids (), while it is understood that corresponds to the elastic effects being as important as the viscous effects, and for the elastic effects dominate the flow over the viscous effects.
The relative importance of surface tension effects (usually for polymer solutions) is assessed by the capillary number, defined by where is the surface tension. For very viscous fluids, such as polymer melts, the surface tension effects are negligible (), and the boundary terms, including a force balance with the capillary forces, can be set to 0.
The relative importance of each term in the energy equation is assessed through a variety of dimensionless groups .
The Peclet number is defined by
The Peclet number is a measure of convective heat transfer with regard to conductive heat transfer. High Pe values indicate a flow dominated by convection. Another group related to Pe is the Graetz number defined by where is the axial length of the die. The Graetz number can be understood as the ratio of the time required for heat conduction from the center of the capillary to the wall and the average residence time in the capillary. As with Pe, a large value of Gz means that heat convection in the flow direction is more important than conduction toward the walls.
The Nahme number is defined by
The Nahme number is a measure of viscous dissipation effects compared with conduction; hence it is an indicator of coupling of the energy and momentum equations. For values of Na > 0.1–0.5 (depending on geometry and thermal boundary conditions), the viscous dissipation leads to considerable coupling of the conservation equations, and a nonisothermal analysis is necessary.
The relative importance of heat transfer mode at the boundaries is expressed in terms of the dimensionless Biot number defined by where is the local radius (gap), is some temperature of the surroundings, and is the local boundary wall temperature. A high value of Biot () approaches isothermal conditions (), while a low value of Biot () describes poor heat transfer to the surroundings (nearly adiabatic case, for which ). Usual Biot values in highly viscous flows inside dies or other processing equipment range between l0 and 100 .
For engineering calculations, the specific heat flux is often described by the Nusselt number where is a heat transfer coefficient. However, as explained by Winter , the Nusselt number is not adequate for describing the wall heat flux in flows with significant viscous dissipation.
4.4. Boundary Conditions
The solution of the conservation equations (44)–(46) and constitutive equation (47) (or whatever viscoelastic K-BKZ model is used for the stresses) is only possible after a set of boundary conditions (BCs) has been imposed on the flow domain. Boundary conditions for flow analysis are highly dependent on the problem at hand, and as such they defy a complete description for all polymer processing applications. However, a rough guide that encompasses most of the types of boundary conditions used in the past follows.
For steady-state problems, the set of equations is elliptic for viscous flows and elliptic-hyperbolic for viscoelastic flows. Elliptic problems have boundary conditions everywhere in the perimeter of the domain, while hyperbolic problems are more difficult to determine their boundary conditions and may need some degree of trial and error. This is especially true at the outflow boundaries, which are more often than not “artificial” or “computational” boundaries, arbitrarily set to reduce the computational domain.
For unsteady-state problems, the set of equations is parabolic due to time, and it also requires initial conditions at time . Then the solution proceeds in time until a steady state is reached (if such exists).
The boundary conditions can be either “fixed” or “natural”. These types refer, respectively, to the primary variables (velocities, pressures, and temperatures) or variables involving their derivatives (stresses, surface tractions, heat fluxes, etc.).
The usual flow boundary conditions in polymer processing are as follows:(a)along the domain entry, a fully developed velocity profile is imposed, according to the assumed constitutive model and corresponding to the apparent shear rate , which is in turn related to the volumetric flow rate . If viscoelasticity is involved through some viscoelastic constitutive model, then the fully developed stress profiles have to be imposed as well;(b)along the centerline (if one exists, as is the case in axisymmetric flows), and because of symmetry, the radial velocity component is set to zero, as well as the shear stresses;(c)along solid walls, usually the no-slip velocity boundary condition is imposed, which states that the velocity of the fluid is the same as that of the boundary, that is, zero if the boundary is stationary, or non-zero if the boundary is moving. In cases where the fluid slips at the wall, as is the case with some polymers , then a slip law has to be assumed based on measurements, which relates the tangential velocity to the tangential components of the stress tensor, while the normal velocity is set to 0;(d)along the domain exit, it is not clear what are the correct or physical boundary conditions for all situations. The best candidate appears to be the “open” or “free” boundary condition (FBC) advocated by Papanastasiou et al. , which basically assumes an extrapolation of the governing equations to the artificial exit boundary. However, the vast majority of the computations assume a long enough domain, where they impose zero surface tractions and zero transverse velocity (assuming implicitly a fully developed profile at exit). For viscoelastic models, fully developed stresses based on the model at hand are used, unless there is a known force or velocity imposed at the exit boundary;(e)in problems with free surfaces, and especially for polymer melts due to their very viscous character (zero surface tension assumed), zero surface tractions are imposed along with a kinematic boundary condition of no flow normal to the surface, that is, , where is the unit outward normal vector to the surface.
For the thermal boundary conditions, the situation is even more difficult to describe due to the many types of thermal conditions used in polymer processing. However, in the vast majority of computations, the following set of boundary conditions is a good representation of what has been applied, based on the previous flow sets:(a)along the domain entry, a set (quite often constant) temperature profile is assumed, sometimes based on measurements or settings;(b)along the centerline (if one exists, as is the case in axisymmetric flows), and because of symmetry, the heat flux is set equal to zero;(c)along solid walls, the surfaces are assumed either as isothermal walls (a set temperature) or as adiabatic walls (heat flux set to 0) or a heat balance between the fluid and the solid boundary [60, 63]. In the latter case, a local Biot number can then be calculated, which is neither 0 (adiabatic walls) nor (isothermal walls), but may range between 10 and 100. Other types of wall thermal boundary conditions involve a known heat flux at the wall based on measurements of an effective heat transfer coefficient, but this is also tantamount to having a non-zero local Biot number;(d)along the domain exit, the same comments apply as above, regarding the flow BCs, with the best candidate being the “open” or “free” BC. However, the majority of computational problems have assumed a long enough domain so as to impose a zero heat flux at the exit;(e)in problems with free surfaces, a zero heat flux is usually imposed, that is, , or a heat balance according to where is a convective heat transfer coefficient to the ambient cooling medium (e.g. air) of temperature , and is the unknown free surface temperature.
For unsteady-state processes, initial conditions are also needed.
5. Method of Solution
5.1. A Brief Literature Survey
It is clear from the start that integral constitutive equations of the K-BKZ type are not trivial. On the contrary, they constitute a major numerical challenge as they have to be solved together with the conservation equations for real polymer flows. Obviously, such a daunting task has kept the computational rheology community on its feet for the better part of the last 30 or so years, starting in 1980 with the pioneering work of Viriyayuthakorn and Caswell , who devised the first finite element technique for integral viscoelastic models. Since then many groups around the world have tackled the issue and many dedicated people have contributed towards a much better state of affairs 30 years later. This was also made possible by the well-known advances in computational power offered by digital computers.
The review article by Keunings  captures in an eloquent and precise way the developments made with the Finite Element Method (FEM) for integral constitutive equations up to 2003. Here we follow Keunings  and pay attention to some interesting developments associated with real polymer flows.
After the work of Viriyayuthakorn and Caswell  who solved the integral Maxwell model, Papanastasiou et al.  devised a coupled streamline FEM (CS-FEM) to solve the K-BKZ/PSM model. In CS-FEM the governing equations are solved simultaneously for the whole set of primary variables with the Newton-Raphson iterative technique. The memory integral is evaluated along particle paths (pathlines, see Figure 3), that are unknown a priori. Problems with storage requirements were encountered and this elegant method was not pursued any further.
A decoupled Eulerian-Lagrangian approach was then pursued, wherein the computation of the viscoelastic stresses is performed separately from that of the flow kinematics. This requires a Picard (or direct substitution) iterative scheme, which is slow to converge as it has linear convergence characteristics. Dupont et al.  used this method to solve the integral Maxwell fluid and the Doi-Edwards model, while later Dupont and Crochet  solved with the same method the K-BKZ/PSM model for an LDPE melt. Meanwhile, Luo and Tanner  had developed a streamline element FEM (SE-FEM) to compute the stresses along unknown a priori streamlines, and with this method they solved the integral Maxwell model and the K-BKZ/PSM model for flows with open streamlines (no recirculation present). This work was considered a breakthrough because for the first time the authors were able to achieve convergence for high enough flow rates, as those encountered in real polymer melt flows. This was attributed to the realistic behavior of the K-BKZ model and the accuracy of their integration scheme. Luo and Tanner  went further to present and solve the K-BKZ/L-T model in extrusion flows of the IUPAC-LDPE melt.
The SE-FEM was modified by Luo and Mitsoulis  to account for both open and closed streamlines (recirculation present) by removing the requirement to construct streamlines in the flow field. Luo and Mitsoulis  used this method to also solve the now considered as a benchmark problem for integral constitutive equations, namely, the flow of the IUPAC-LDPE melt in extrusion dies with the integral K-BKZ/PSM model.
The same problem was also solved by Bernstein et al.  and Feigl and Ottinger  using similar integrating schemes for the viscoelastic stresses. At this point it is to be noted that at least 4 different groups around the world (Crochet’s in Belgium, Tanner’s in Australia, Mitsoulis’s in Canada, and Bernstein’s in the USA) employing different codes were able to solve the same benchmark problem of die flow of the IUPAC-LDPE melt with the K-BKZ/PSM or its variants, obtaining similar (if not identical) results. In this way a confidence was built in the different schemes for the integration of the viscoelastic stresses according to K-BKZ-type models.
At the same time, a Lagrangian Integral Method (LIM) was advocated by Hassager and Bisgaard . As its name indicates, LIM is based on the Lagrangian formulation of the conservation laws. The primary kinematic variables are the time-dependent positions of the fluid elements, while the computational domain is a deforming material volume. The latter is discretized by means of a finite element mesh that deforms with the flow. A typical flow simulation with LIM amounts to solving a transient problem, given the initial particle positions and deformation pre history. LIM is thus a coupled method capable of solving transient flow problems. Steady-state flows are computed as the long-time limit of a transient problem. As all Lagrangian techniques, LIM readily applies to flows with free surfaces. Over the years, the method has been refined and extended to treat three-dimensional flows (Rasmussen and Hassager [75, 76], Rasmussen [77, 78]). To this date, it remains one of the few cases (if not the only one) where integral constitutive equations are solved for transient 3D problems.
In the review article by Keunings  there are also references to the method of deformation fields by Peters et al.  and to methods applied for integrodifferential models derived from molecular theory (namely, the Doi-Edwards models). However, these methods are beyond the scope of the present paper, and interested readers are kindly asked to consult the excellent review by Keunings .
5.2. The Decoupled Eulerian-Lagrangian Approach
In what follows we present in some detail the numerical technique implemented with Picard iterative schemes, namely the decoupled Eulerian-Lagrangian approach, which has been most widely used in numerical simulations of polymer flows with the variants of the K-BKZ model, namely, the PSM and the L-T models.
In the decoupled techniques the computation of the viscoelastic stresses is performed separately from that of the flow kinematics. These techniques are based on an Eulerian-Lagrangian approach, which combines the computation of Eulerian velocity and pressure fields with the Lagrangian evaluation of the strain history along particle trajectories. The decoupled Eulerian-Lagrangian techniques are aimed at steady-state flows only. They have been under development since the end of the 1970s, and most of the fundamental ideas have been reviewed in detail by Crochet et al.  and Keunings .
5.2.1. Iterative Strategy
The iterative strategy consists of the following steps:(1)using the velocity field computed at the previous iteration, integrate the constitutive equation to update the viscoelastic stresses;(2)using the viscoelastic stress computed in step 1, update the kinematics by solving the conservation laws;(3)check for convergence; if needed, return to step 1 for another iteration.
It was realized early on  that the viscoelastic stresses can be split into a viscous (Newtonian) component and a purely viscoelastic component by adding and subtracting the viscous component in the momentum equation. This scheme has been called the elastic-viscous split stress (EVSS) scheme and it is widely used in viscoelastic simulations [80, 81]. Effectively, the extra stress in the momentum equation is replaced by where is an arbitrary Newtonian viscosity, and is a control parameter between 0 and 1 (under-relaxation parameter). For , the flow problem is purely Newtonian, while the original viscoelastic equation is recovered for .
Let denote the viscoelastic stress computed at the th iteration. Then, for creeping flows, amounts to solving for the updated velocity and pressure fields and , respectively. During the iterative process, the control parameter is progressively increased from 0 to 1, so that a solution to the original viscoelastic equations is finally obtained. This strategy is similar to the incremental loading procedure used in non-linear elasticity, where now the “load” is the viscoelastic stresses. In all cases, the solution starts from the Newtonian solution () and proceeds from there.
The above strategy was able to reproduce the exact analytical solutions for the integral Maxwell fluid (IMX) in Poiseuille flow for values of Wi up to 2, but not higher. This is called the High-Weissenberg Number Problem (HWNP)  that had plagued viscoelastic simulations for almost all of the 1980s. A major breakthrough was achieved by the adaptive-viscous split stress (AVSS) scheme proposed from Tanner’s group , whereby the reference viscosity at element level is given by where is the element size, is the maximum elastic stress value in the element, and is the maximum velocity value in the element. With this definition of changing per element, no upper limit of convergence was detected for the benchmark problem of IMX Poiseuille flow, and solutions were attainable at much higher Wi values for other problems as well .
5.2.2. Finite Element Equations
of the decoupled strategy is a Newtonian flow problem defined by (76), where is treated as a pseudo-body force that is known from the previous iteration. The corresponding Galerkin finite element equations read In the above, is the flow domain, and is part of the boundary with outward unit normal vector where the contact force (surface traction) is specified; the discrete velocity and pressure fields are approximated by where and are unknown nodal values, and are given shape functions, and and are the number of velocity and pressure nodes, respectively. In (78), , .
The pseudo-body force integral in the right-hand side of the Galerkin momentum equations is computed using the viscoelastic stress and velocity fields known from the previous iteration. To this end, we must somehow evaluate the viscoelastic stress at all integration points of the finite element mesh; this defines Step 1 of the decoupled strategy, which we discuss next.
5.2.3. Integration of the Constitutive Model
Computation of the viscoelastic stress at each integration point of the mesh is performed in three basic steps, using the Lagrangian formulation of the constitutive model.(1)Particle tracking: using the steady-state velocity field known from the previous iteration, compute the past (i.e. upstream) trajectory and the travel time of the integration point.(2)Strain evaluation: at selected past times, compute the deformation gradient tensor and from it the integrand of the constitutive model.(3)Stress evaluation: compute the memory integral numerically along the past trajectories, using the results of the first and second steps.
The last task is the simplest one. In a steady-state flow, the displacement function is independent of and may be written as , where is the time lapse . This implies that . With a single-exponential memory function (although multiple relaxation times are easily handled), the generic integral model becomes where . Following the early work of Viriyayuthakorn and Caswell , a possible approach is to use a Gauss-Laguerre integration rule to approximate the memory integral: where are the roots of the Laguerre polynomial, and are the weights of the quadrature rule. In practice, is of order 10. This approximation implies that the deformation need only be computed at the discrete time lapses . Obviously, ever larger strains must be evaluated when the memory of the fluid increases. The Gauss-Laguerre approach has been extended to finite and infinite relaxation spectra by Malkus and Bernstein . More flexible integration techniques, though also more expensive, have been introduced by Dupont et al.  and Luo and Tanner . The time integral equation (81) is transformed into a line integral along the past trajectory; the latter is subdivided into segments through which the fluid particle travels in a time shorter than the relaxation time , and a Gauss quadrature rule is used to compute the integral along each segment. The backward integration is stopped once the marginal contribution of a segment is less than some specified tolerance. Interestingly, small relaxation times require a finer segmentation in order to capture the recent deformation history.
In principle, tracking of past particle positions and computation of the strain history require the integration of the kinematic equations backward along each particle trajectory, with the respective initial conditions
The particle tracking procedure necessary with the above equations presents a major difficulty in computations with the K-BKZ integral model. The early numerical schemes reviewed by Crochet et al.  had severe numerical problems with these two tasks. A first satisfactory solution was advanced by Bernstein et al.  for two-dimensional planar flows. Briefly, it consists in using a special low-order finite element made of four triangles to compute the velocity field. The velocity finite element approximation is such that both tracking and strain history calculations can be performed analytically within each triangle. The price to pay for this nice result is the relatively low accuracy of the computed velocity field, and also the fact that the special element has spurious pressure modes. Extension of this approach to axisymmetric flows is reported by Bernstein et al. .
Luo and Tanner  introduced another approach based on the concept of streamline finite elements. These are quadrilateral elements which have a pair of opposed sides that are aligned with streamlines. From the computation of the stream function using the current velocity field, which amounts to solving the Poisson equation, , the mesh is updated at each iteration so that the nodes (and thus the integration points) always lie along selected streamlines. A parametric representation of past trajectories is thus readily available in each element. The authors then compute the deformation history by solving the kinematic equation (84) backward along each discrete streamline using a 4th-order Runge-Kutta method. This approach is both fast and accurate, but it cannot handle recirculation regions. This problem was circumvented by Luo and Mitsoulis , who did not use streamline elements but integrated the tracking problem (see (84)) by means of a second-order scheme, valid for both open and closed streamlines, which is independent of the type of element.
The tracking procedure developed by Goublomme et al.  is also independent of the type of element. Pathlines are computed on an element-by-element basis, by means of a 4th-order Runge-Kutta integration of (83) within the parent element. This eliminates most of the complicated geometrical problems of earlier tracking schemes. In order to compute the deformation history, the authors follow the work of Dupont et al. , who showed that, for a steady-state flow, the deformation gradient can be computed by means of the velocity vectors at Lagrangian times and and values of a scalar quantity which obeys a first-order differential equation involving the velocity field along the pathline. Similarly for the tracking itself, Goublomme et al.  integrate the equation for in the parent element. Very efficient implementations of this method on message-passing parallel computers have been proposed by Aggarwal et al.  and Henriksen and Keunings .
5.3. Some Issues Arising in Viscoelastic Computations
Implementation of a finite element formulation for the mass and momentum equations uses the primitive-variables approach, that is, velocities and pressure (in 2D flows this is called the formulation). For viscoelastic formulations, the stresses are also needed as discrete variables, and this leads to a mixed-variable approach (called formulation or EVSS for elastic-viscous split stress). A better formulation requires also the rates of strain as extra variables, thus leading to an enhanced mixed-variable approach (called formulation or DEVSS-G for discontinuous elastic-viscous split stress-strain rate). Variations of these also exist. For the energy formulation, the temperature is the single primitive field variable. Special streamline-upwind/Petrov-Galerkin (SU/PG) techniques are used for highly convective flows (high Pe numbers; Mitsoulis et al. ). More details about the SU/PG scheme can be found in the landmark paper by Marchal and Crochet .
At this point it is perhaps instructive to give a feel of the complexity of solving flow problems in polymer processing with viscous or viscoelastic constitutive models, and in the latter case the differences between using differential or integral models to describe polymer melts. We take as an example a 2-D flow problem and the FEM employing a typical 9-node Lagrangian quadrilateral element, as shown in Figure 7. A viscous problem, based on the formulation, would require 22 dof (degrees of freedom) per element (, , and variables). If the flow problem is also coupled with the thermal problem, then we have 31 dof/elem ( variables). A serendipity element is cheaper as it has only 8 nodes (it lacks the centroid node), thus giving 20 dof/elem (flow/+thermal problem).
Now for a viscoelastic problem, with one (1) relaxation mode, the stresses and the strain rates have to be added to the nodal unknowns. In 2-D flows, we distinguish between planar and axisymmetric flows . These extra nodal unknowns are defined at the corner nodes (due to linear interpolation), thus adding stresses and strain rates, a total of 24 extra dof (planar); and stresses and strain rates, a total of 32 dof (axisymmetric). Thus, the total dof/element are dof/elem (flow/+thermal planar problem) and dof/elem (flow/+thermal axisymmetric problem). Note that these numbers are for a single relaxation model.
For the 8 relaxation modes describing the IUPAC-LDPE melt  or the polymer melts of Figures 4–6, the corresponding numbers become 214(223) dof/elem (flow/+thermal planar problem) and 278(287) dof/elem (flow/+thermal axisymmetric problem). These numbers are given collectively in Table 2 and are necessary for solving any problem with a differential viscoelastic model, for example, the popular “pom-pom” model .
It is then obvious that even for a sparse FEM mesh of a 1000 elements the total number of dof climbs to . So it is not surprising that even in today’s computers there are only very few viscoelastic problems that have been solved with the full spectrum and differential viscoelastic models (like the “pom-pom”) even for simple 2-D flows.
The situation is different with integral constitutive models, such as the K-BKZ/PSM model or the K-BKZ/L-T model. In this case, the formulation remains with the same number of dof/element as in viscous flows. The stresses are then calculated a posteriori along streamlines according to the integral using a 15-point Gauss-Laguerre quadrature suitable for exponentially fading functions . The summation used in the integration is very fast with digital computers, and it does not make much difference in computational time by using either 1 or 8 relaxation modes. This is a major advantage of integral constitutive equations! Most of the computational time is used for the solution of the problem, while the a posteriori computation of the stresses takes approximately an equal amount of CPU time (at least this is the case for the middle range of flow rates; at low flow rates the Newtonian-like behavior of polymer melts makes the computation of stresses extremely fast; at the other end of very high flow rates, the computation of stresses becomes most time consuming). Thus, it was possible to solve many 2-D flow problems by the year 2000 in the personal computers (PCs) of the day, as evidenced in a series of papers by Mitsoulis and his co-workers .
As an example we give here the case of flow through a contraction of the IUPAC-LDPE melt A, using the K-BKZ/L-T model with 8 relaxation modes and the data given by Tanner , and employing the computational method of streamline integration developed by Luo and Mitsoulis . In the year 2000, working on a PC Pentium II at 300 MHz with 128 MB RAM, for a mesh with 640 elements it was taking 20 CPU seconds for the frontal solution of the system of equations and another 20 CPU seconds for the calculation of stresses for each iteration. To get a solution at an elevated flow rate (corresponding to an apparent shear rate s−1), about 1000 iterations were needed for a total of 11 CPU hours. In today’s computers (Intel Core2 Duo at GHz with 2 GB RAM), the same problem can be solved in the same overall time but with 10 times the number of finite elements (6400) and the results are the same, just smoother. Thus, it has been possible to solve viscoelastic problems of multimode fluids, such as polymer melts, in more complex geometries, such as those encountered in polymer processing, as will be discussed below.
This K-BKZ/PSM or L-T integral model has been used in numerical flow simulations for a number of flow problems more or less successfully (see, e.g., Luo and Tanner , Dupont and Crochet , Bernstein et al. , Barakos and Mitsoulis , Sun et al. , and Ansari et al. [45, 46]). The review by Keunings  on the subject gives a list of problems solved with this model through numerical simulation, including many flows from polymer processing operations. Other flows solved with a number of different constitutive equations can be found in an excellent book on computational rheology .
6. Some Applications of the Model
6.1. Flow Patterns in Contraction Flows
The flow of polymer melts through abrupt contractions has been a benchmark problem in computational rheology ever since visualization data on polyethylenes appeared in a capillary rheometer more than 50 years ago from Bagley and Birks  in 1960. The differences in behavior between an LDPE and a HDPE melt regarding vortex development, as shown in Figure 8, were a big challenge for the theoreticians and the numerical analysts to reproduce by an appropriate rheological model this difference in behavior, which is obviously attributed to viscoelasticity. It suffices to say that any viscous model fails miserably to capture this behavior, in particular the big vortices of the LDPE melt.
With the K-BKZ/PSM model and the method developed by Luo and Mitsoulis  this problem was successfully solved, see Mitsoulis . For the same shear stress level at the wall ( MPa), the simulations showed a remarkable resemblance to the experimental patterns of the two melts as shown in Figure 9. The data for the LDPE are those for the IUPAC-LDPE melt . Those of HDPE are given in . This is a very good indication of the ability of the K-BKZ model to predict unusual non-Newtonian flow behavior for two major industrial polymers. After all, this was the original idea behind developing such models.
6.2. Pressure Drop in Contraction Flows
In capillary flow of molten polymers generated by means of a capillary rheometer, there is a large pressure drop associated with the flow in the entrance (major) and exit (minor) regions. If the pressure in the reservoir is the quantity measured to determine the wall shear stress in the part of the capillary where flow is fully developed, these two excess pressure losses, collectively known as end pressure, should be taken into account (Dealy and Wissbrun ). The end pressure is also used to estimate the extensional viscosity of polymers, a method well practised in industry (Cogswell [96, 97]). Therefore, it is significant to understand the origin of this excess pressure and consequently be able to predict it.
Figure 10 plots the axial pressure variation in a capillary die including both its entrance and exit regions. It can be seen that the total pressure drop, , consists of two components and may be written as where is the total pressure drop from the reservoir to the capillary exit, is the pressure drop over the length of the capillary where the flow is fully developed, and is the excess pressure drop due to the entrance and exit flows. Bagley  has suggested an empirical method of calculating this combined excess pressure . The results from this procedure are customarily presented in terms of the Bagley correction or end correction, , defined as where is the wall shear stress in the die for fully developed flow. In a capillary die of radius and length (see Figure 10), the shear stress, , can be related to the Bagley correction, , the overall pressure drop, , and the derivative of the pressure, , along the die axis according to Bagley : A graph of versus for a constant apparent shear rate is the well-known Bagley plot, where can be found by extrapolation of straight lines to .
This important phenomenon exhibited by polymer melts had not been successfully predicted by any viscoelastic constitutive model. On the contrary, the early efforts by simple models gave less pressure losses than even the Newtonian fluids in contrast with experimental evidence.
The situation was recently overturned by the application of the K-BKZ/PSM or K-BKZ/L-T model for the two polyethylene melts of Section 3. Figure 11 shows the good agreement obtained for the two melts, namely, the LDPE melt  and the HDPE melt . In doing the simulations, all effects have been accounted for, such as temperature (nonisothermal simulations), pressure dependence of viscosity (important for LDPE), and slip at the wall (important for HDPE). More information can be found in the two publications. Therefore, use of the K-BKZ model in its variant types (PSM or L-T) was successful in correctly simulating the pressure drops in rheometry, an important phenomenon that eluded proper prediction so far.
7. Conclusions and Future Prospects
The present paper reviewed the 50 years since the appearance of the K-BKZ model in the rheological community around 1962. This review followed and borrowed from Tanner’s article , which had reviewed the relevant publications for the 25th anniversary of the model in 1988. The numerical methods section followed and borrowed from Keunings’ article  in 2003. The updating of the works showed the following.(1)The K-BKZ model has had a strong influence in the rheological community in the last 50 years, with an increasing number of citations (reaching 2000) and a reputation for good results.(2)The interest by other groups peaked around the 25th anniversary of the article (1986–1990) with different groups around the world working towards a numerical implementation of the model and an emphasis on its predictions for real polymer flows.(3)There were important improvements of the model following the idea of irreversibility by Wagner et al. , a more complete description by Luo and Tanner , and a new damping function for planar flows by Olley .(4)The numerical implementation saw the emergence of new schemes that were more general (valid for recirculation patterns)  and were extended to transient flows (LIM) [74–76] and 3D flows . To this effect the continuing increasing power of computers helped significantly.(5)Many works focused on simulating real data and phenomena associated with polymer melt flows in rheology and polymer processing, in most cases with considerable success .(6)Important new efforts focused on molecularly-based integral equations based on the Doi-Edwards theories [34–42].
The challenges ahead are likely to continue along the molecularly-based models, although efforts will also be directed towards numerical solutions of the K-BKZ/PSM or L-T variants for three-dimensional, time-dependent flows, perhaps with the Newton-Raphson method for better precision. The method developed by Dimakopoulos et al.  is extremely useful towards that end. The main advantage of integral models remains the inclusion of many relaxation times (or an infinite spectrum) without having extra degrees of freedom associated with the stresses.
As Tanner  wrote presciently in 1988, “I do not think the theory will fade away rapidly since it is the optimal type of single-integral equation if a sufficiently limited range of flows is to be modeled. Therefore I look forward to 2012 and the 50th anniversary of the KBKZ theory”. In the same spirit, we can also say that we are looking forward to 2022 and the 60th (Diamond Jubilee) anniversary of the K-BKZ theory.
Financial assistance from the Program for Basic Research “THALES” of the Ministry of Education of Greece is gratefully acknowledged.
- R. I. Tanner, Engineering Rheology, Oxford University Press, Oxford, UK, 2nd edition, 2000.
- R. I. Tanner and K. Walters, Rheology: An Historical Perspective, Elsevier, Amsterdam, The Netherlands, 1998.
- Heraclitus, “On Nature,” 2012, http://en.wikipedia.org/wiki/Heraclitus.
- C. W. Macosko, Rheology: Principles, Measurements, and Applications, VCH Publishers, New York, NY, USA, 1994.
- 2012, http://www.rheology-esr.net/ICR2012.
- 2012, http://www.journals.elsevier.com/journal-of-non-newtonian-fluid-mechanics/.
- B. Bernstein, E. A. Kearsley, and L. J. Zapas, “A study of stress relaxations with finite strain,” Transactions of The Society of Rheology, vol. 7, pp. 391–410, 1963.
- A. Kaye, Non-Newtonian Flow in Incompressible Fluids, Note No. 134, College of Aeronautics, Cranfield, UK, 1962.
- R. I. Tanner, “From A to (BK)Z in constitutive relations,” Journal of Rheology, vol. 32, no. 7, pp. 673–702, 1988.
- 2012, http://sub3.webofknowledge.com.
- A. S. Lodge, “A network theory of flow birefringence and stress in concentrated polymer solutions,” Transactions of the Faraday Society, vol. 52, pp. 120–130, 1956.
- L. R. G. Treloar, The Physics of Rubber Elasticity, Oxford University Press, New York, NY, USA, 2nd edition, 1958.
- C. Truesdell, “The mechanical foundations of elasticity and fluid mechanics,” Journal of Rational Mechanics and Analysis, vol. 2, pp. 125–300, 1952.
- C. Truesdell, “Two measures of vorticity,” Journal of Rational Mechanics and Analysis, vol. 3, pp. 593–616, 1953.
- B. Bernstein, E. Kearsley, and L. Zapas, “Elastic stress-strain relations in perfect elastic fluids,” Transactions of The Society of Rheology, vol. 9, pp. 27–39, 1965.
- L. J. Zapas and T. Craft, “Correlation of large longitudinal deformations with different strain histories,” Journal of research of the National Bureau of Standards A, vol. 69, pp. 541–546, 1965.
- B. Bernstein, E. A. Kearsley, and L. J. Zapas, “Thermodynamics of perfect elastic fluids,” Journal of research of the National Bureau of Standards B, vol. 68, pp. 103–113, 1964.
- A. E. Green and R. S. Rivlin, “The mechanics of non-linear materials with memory,” Archive for Rational Mechanics and Analysis, vol. 1, pp. 1–21, 1957.
- W. Noll, “A mathematical theory of the mechanical behavior of continuous media,” Archive for Rational Mechanics and Analysis, vol. 2, no. 1, pp. 197–226, 1958.
- A. C. Pipkin, “Small finite deformations of viscoelastic solids,” Reviews of Modern Physics, vol. 36, no. 4, pp. 1034–1041, 1964.
- J. L. White and N. Tokita, “An additive functional theory of viscoelastic deformation with application to amorphous polymers, solutions and vulcanizates,” Journal of the Physical Society of Japan, vol. 22, no. 3, pp. 719–724, 1967.
- R. S. Rivlin and K. N. Sawyers, “Nonlinear continuum mechanics of viscoelastic fluids,” Annual Review of Fluid Mechanics, vol. 3, pp. 117–146, 1972.
- R. B. Bird, R. C. Armstrong, and O. Hassager, Dynamics of Polymeric Liquids, vol. 1 of Fluid Mechanics, John Wiley & Sons, New York, NY, USA, 2nd edition, 1987.
- R. G. Larson, The Structure and Rheology of Complex Fluids, Oxford University Press, 1999.
- A. S. Lodge, Elastic Liquids, Academic Press, London, UK, 1964.
- J. Meissner, “Basic parameters, melt rheology, processing and end-use properties of three similar low density polyethylene samples,” Pure and Applied Chemistry, vol. 42, pp. 551–623, 1975.
- M. H. Wagner, “Analysis of time-dependent non-linear stress-growth data for shear and elongational flow of a low-density branched polyethylene melt,” Rheologica Acta, vol. 15, no. 2, pp. 136–142, 1976.
- M. H. Wagner, T. Raible, and J. Meissner, “Tensile stress overshoot in uniaxial extension of a LDPE melt,” Rheologica Acta, vol. 18, no. 3, pp. 427–428, 1979.
- D. D. Joseph, International Symposium on Viscoelastic Fluids, Tobago, West Indies, 1994.
- A. C. Papanastasiou, L. E. Scriven, and C. W. Macosko, “Integral constitutive equation for mixed flows: viscoelastic characterization,” Journal of Rheology, vol. 27, no. 4, pp. 387–410, 1983.
- X. L. Luo and R. I. Tanner, “Finite element simulation of long and short circular die extrusion experiments using integral models,” International Journal for Numerical Methods in Engineering, vol. 25, pp. 9–22, 1988.
- M. H. Wagner, “Elongational behaviour of polymer melts in constant elongation-rate, constant tensile stress, and constant tensile force experiments,” Rheologica Acta, vol. 18, no. 6, pp. 681–692, 1979.
- P. Olley, “An adaptation of the separable KBKZ equation for comparable response in planar and axisymmetric flow,” Journal of Non-Newtonian Fluid Mechanics, vol. 95, no. 1, pp. 35–53, 2000.
- M. Doi and S. F. Edwards, Theory of Polymer Dynamics, Oxford University Press, 1986.
- M. Doi and S. F. Edwards, “Dynamics of concentrated polymer systems, Parts I-IV,” Journal of the Chemical Society, Faraday Transactions II, vol. 74, pp. 1789–1832, 1978.
- M. Doi and S. F. Edwards, “Dynamics of concentrated polymer systems, Parts I-IV, J,” Journal of the Chemical Society, Faraday Transactions II, vol. 75, pp. 38–54, 1979.
- C. F. Curtiss and R. Byron Bird, “A kinetic theory for polymer melts. II. The stress tensor and the rheological equation of state,” The Journal of Chemical Physics, vol. 74, no. 3, pp. 2026–2033, 1980.
- P. K. Currie, “Constitutive equations for polymer melts predicted by the Doi-Edwards and Curtiss-Bird kinetic theory models,” Journal of Non-Newtonian Fluid Mechanics, vol. 11, no. 1-2, pp. 53–68, 1982.
- D. W. Mead, R. G. Larson, and M. Doi, “A molecular theory for fast flows of entangled polymers,” Macromolecules, vol. 31, no. 22, pp. 7895–7914, 1998.
- T. C. B. McLeish and R. G. Larson, “Molecular constitutive equations for a class of branched polymers: the pom-pom polymer,” Journal of Rheology, vol. 42, no. 1, pp. 81–110, 1998.
- G. Ianniruberto and G. Marrucci, “A simple constitutive equation for entangled polymers with chain stretch,” Journal of Rheology, vol. 45, no. 6, pp. 1305–1318, 2001.
- M. H. Wagner, P. Rubio, and H. Bastian, “The molecular stress function model for polydisperse polymer melts with dissipative convective constraint release,” Journal of Rheology, vol. 45, no. 6, pp. 1387–1412, 2001.
- O. Hassager, J. M. R. Marin, K. Yu, and H. K. Rasmussen, “Polymeric liquids in extension: fluid mechanics or rheometry?” Rheologica Acta, vol. 49, no. 6, pp. 543–554, 2010.
- O. Hassager and R. Hansen, “Constitutive equations for the Doi-Edwards model without independent alignment,” Rheologica Acta, vol. 49, no. 6, pp. 555–562, 2010.
- M. Ansari, Th. Zisis, S. G. Hatzikiriakos, and E. Mitsoulis, “Capillary flow of low-density polyethylene,” Polymer Engineering & Science, vol. 52, pp. 649–662, 2012.
- M. Ansari, S. G. Hatzikiriakos, and E. Mitsoulis, “Slip Effects in HDPE Flows,” Journal of Non-Newtonian Fluid Mechanics, vol. 167-168, pp. 18–29, 2012.
- T. Kajiwara, G. Barakos, and E. Mitsoulis, “Rheological characterization of polymer solutions and melts with an integral constitutive equation,” International Journal of Polymer Analysis and Characterization, vol. 1, pp. 201–215, 1995.
- 2012, http://rheology.tripod.com/.
- M. Baumgaertel and H. H. Winter, “Determination of discrete relaxation and retardation time spectra from dynamic mechanical data,” Rheologica Acta, vol. 28, no. 6, pp. 511–519, 1989.
- V. Tirtaatmadja and T. Sridhar, “A filament stretching device for measurement of extensional viscosity,” Journal of Rheology, vol. 37, pp. 1081–1102, 1993.
- G. H. McKinley and T. Sridhar, “Filament-stretching rheometry of complex fluids,” Annual Review of Fluid Mechanics, vol. 34, pp. 375–415, 2002.
- M. L. Sentmanat, “Miniature universal testing platform: from extensional melt rheology to solid-state deformation behavior,” Rheologica Acta, vol. 43, no. 6, pp. 657–669, 2004.
- D. G. Baird and D. I. Collias, Polymer Processing: Principles and Design, Butterworth-Heinemann, Boston, Mass, USA, 1995.
- X. L. Luo and R. I. Tanner, “A pseudo-time integral method for non-isothermal viscoelastic flows and its application to extrusion simulation,” Rheologica Acta, vol. 26, no. 6, pp. 499–507, 1987.
- S. M. Alaie and T. C. Papanastasiou, “Modeling of non-isothermal film blowing with integral constitutive equations,” International Polymer Processing, vol. 8, pp. 51–65, 1993.
- M. Beaulne and E. Mitsoulis, “Effect of viscoelasticity in the film-blowing process,” Journal of Applied Polymer Science, vol. 105, no. 4, pp. 2098–2112, 2007.
- J. M. Dealy and K. F. Wissbrun, Melt Rheology and Its Role in Plastics Processing–Theory and Applications, Van Nostrand Reinhold, New York, NY, USA, 1990.
- H. M. Laun, “Pressure dependent viscosity and dissipative heating in capillary rheometry of polymer melts,” Rheologica Acta, vol. 42, no. 4, pp. 295–308, 2003.
- S. Middleman, Fundamentals of Polymer Processing, McGraw-Hill, New York, NY, USA, 1977.
- H. H. Winter, “Viscous dissipation in shear flows of molten polymers,” Advances in Heat Transfer, vol. 13, no. C, pp. 205–267, 1977.
- S. G. Hatzikiriakos and J. M. Dealy, “Wall slip of molten high density polyethylenes. II. Capillary rheometer studies,” Journal of Rheology., vol. 36, pp. 703–741, 1992.
- T. C. Papanastasiou, N. Malamataris, and K. Ellwood, “New outflow boundary condition,” International Journal for Numerical Methods in Fluids, vol. 14, no. 5, pp. 587–608, 1992.
- E. Mitsoulis, R. Wagner, and F. L. Heng, “Numerical simulation of wire-coating low-density polyethylene: theory and experiments,” Polymer Engineering and Science, vol. 28, no. 5, pp. 291–310, 1988.
- M. Viriyayuthakorn and B. Caswell, “Finite element simulation of viscoelastic flow,” Journal of Non-Newtonian Fluid Mechanics, vol. 6, no. 3-4, pp. 245–267, 1980.
- R. Keunings, “Finite element methods for integral viscoelastic fluids,” in Rheology Reviews, D. Binding and K. Walters, Eds., pp. 167–195, British Society of Rheology, 2003.
- A. C. Papanastasiou, L. E. Scriven, and C. W. Macosko, “A finite element method for liquid with memory,” Journal of Non-Newtonian Fluid Mechanics, vol. 22, no. 3, pp. 271–288, 1987.
- S. Dupont, J. M. Marchal, and M. J. Crochet, “Finite element simulation of viscoelastic fluids of the integral type,” Journal of Non-Newtonian Fluid Mechanics, vol. 17, no. 2, pp. 157–183, 1985.
- S. Dupont and M. J. Crochet, “The vortex growth of a K.B.K.Z. fluid in an abrupt contraction,” Journal of Non-Newtonian Fluid Mechanics, vol. 29, pp. 81–91, 1988.
- X. L. Luo and R. I. Tanner, “A streamline element scheme for solving viscoelastic flowproblems part II: integral constitutive models,” Journal of Non-Newtonian Fluid Mechanics, vol. 22, no. 1, pp. 61–89, 1986.
- X. L. Luo and E. Mitsoulis, “An efficient algorithm for strain history tracking in finite element computations of non-newtonian fluids with integral constitutive equations,” in International Journal for Numerical Methods in Fluids, vol. 11, pp. 1015–1031, 1990.
- X. L. Luo and E. Mitsoulis, “A numerical study of the effect of elongational viscosity on vortex growth in contraction flows of polyethylene melts,” in Journal of Rheology, vol. 34, pp. 309–342, 1990.
- B. Bernstein, K. A. Feigl, and E. T. Olsen, “Steady flows of viscoelastic fluids in axisymmetric abrupt contraction geometry: a comparison of numerical results,” Journal of Rheology, vol. 38, no. 1, pp. 53–71, 1994.
- K. Feigl and H. C. Ottinger, “Flow of a LDPE melt through an axisymmetric contraction: a numerical study and comparison to experimental results,” Journal of Rheology, vol. 38, no. 4, pp. 847–874, 1994.
- O. Hassager and C. Bisgaard, “A Lagrangian finite element method for the simulation of flow of non-newtonian liquids,” Journal of Non-Newtonian Fluid Mechanics, vol. 12, no. 2, pp. 153–164, 1983.
- H. K. Rasmussen and O. Hassager, “Simulation of transient viscoelastic flow,” Journal of Non-Newtonian Fluid Mechanics, vol. 46, no. 2-3, pp. 289–305, 1993.
- H. K. Rasmussen and O. Hassager, “Simulation of transient viscoelastic flow with second order time integration,” Journal of Non-Newtonian Fluid Mechanics, vol. 56, no. 1, pp. 65–84, 1995.
- H. K. Rasmussen, “Time-dependent finite-element method for the simulation of three-dimensional viscoelastic flow with integral models,” Journal of Non-Newtonian Fluid Mechanics, vol. 84, no. 2-3, pp. 217–232, 1999.
- H. K. Rasmussen, “Lagrangian viscoelastic flow computations using the Rivlin-Sawyers constitutive model,” Journal of Non-Newtonian Fluid Mechanics, vol. 92, no. 2-3, pp. 227–243, 2000.
- E. A. J. F. Peters, M. A. Hulsen, and B. H. A. A. Van Den Brule, “Instationary eulerian viscoelastic flow simulations using time separable Rivlin-Sawyers constitutive equations,” Journal of Non-Newtonian Fluid Mechanics, vol. 89, no. 1-2, pp. 209–228, 2000.
- M. J. Crochet, A. R. Davies, and K. Walters, Numerical Simulation of Non-Newtonian Flow, Elsevier, Amsterdam, The Netherlands, 1984.
- R. Keunings, “Simulation of viscoelastic fluid flow,” in Fundamentals of Computer Modelling for Polymer Processing, C. L. Tucker, Ed., pp. 404–469, Hanser Publishers, Munich, Germany, 1989.
- M. G. N. Perera and K. Walters, “Long-range memory effects in flows involving abrupt changes in geometry. Part I: flows associated with I-shaped and T-shaped geometries,” Journal of Non-Newtonian Fluid Mechanics, vol. 2, no. 1, pp. 49–81, 1977.
- R. Keunings, “On the high Weissenberg number problem,” Journal of Non-Newtonian Fluid Mechanics, vol. 20, pp. 209–226, 1986.
- J. Sun, N. Phan-Thien, and R. I. Tanner, “An adaptive viscoelastic stress splitting scheme and its applications: AVSS/SI and AVSS/SUPG,” Journal of Non-Newtonian Fluid Mechanics, vol. 65, no. 1, pp. 75–91, 1996.
- D. S. Malkus and B. Bernstein, “Flow of a curtiss-bird fluid over a transverse slot using the finite element drift-function method,” Journal of Non-Newtonian Fluid Mechanics, vol. 16, no. 1-2, pp. 77–116, 1984.
- B. Bernstein, D. S. Malkus, and E. T. Olsen, “A finite element for incompressible plane flows of fluids with memory,” International Journal for Numerical Methods in Fluids, vol. 5, no. 1, pp. 43–70, 1985.
- A. Goublomme, B. Draily, and M. J. Crochet, “Numerical prediction of extrudate swell of a high-density polyethylene,” Journal of Non-Newtonian Fluid Mechanics, vol. 44, pp. 171–195, 1992.
- R. Aggarwal, R. Keunings, and F. X. Roux, “Simulation of the flow of integral viscoelastic fluids on a distributed memory parallel computer,” Journal of Rheology, vol. 38, no. 2, pp. 405–419, 1994.
- P. Henriksen and R. Keunings, “Parallel computation of the flow of integral viscoelastic fluids on a heterogeneous network of workstations,” International Journal for Numerical Methods in Fluids, vol. 18, no. 12, pp. 1167–1183, 1994.
- J. M. Marchal and M. J. Crochet, “A new mixed finite element for calculating viscoelastic flow,” Journal of Non-Newtonian Fluid Mechanics, vol. 26, no. 1, pp. 77–114, 1987.
- E. Mitsoulis, “Computational polymer processing,” in Modeling and Simulation in Polymers, P. D. Gujrati and A. I. Leonov, Eds., Chapter 4, pp. 127–195, Wiley-VCH, Weinheim, Germany, 2010.
- G. Barakos and E. Mitsoulis, “Numerical simulation of extrusion through orifice dies and prediction of Bagley correction for an IUPAC-LDPE melt,” Journal of Rheology, vol. 39, no. 1, pp. 193–209, 1995.
- R. G. Owens and T. N. Phillips, Computational Rheology, Imperial College Press, London, UK, 2002.
- E. B. Bagley and A. M. Birks, “Flow of polyethylene into a capillary,” Journal of Applied Physics, vol. 31, no. 3, pp. 556–561, 1960.
- E. Mitsoulis, “Effect of viscoelasticity in fountain flow of polyethylene melts,” International Polymer Processing, vol. 24, pp. 439–451, 2009.
- F. N. Cogswell, “Measuring the extensional rheology of polymer melts,” Transactions of The Society of Rheology, vol. 16, no. 3, pp. 383–403, 1972.
- F. N. Cogswell, “Polymer melt rheology. A guide for industrial practice,” 1981.
- E. B. Bagley, “End corrections in the capillary flow of polyethylene,” Journal of Applied Physics, vol. 28, no. 5, article 624, 4 pages, 1957.
- Y. Dimakopoulos, J. Papaioannou, and J. Tsamopoulos, “Cavity growth in pressure sensitive adhesive materials: 3D finite element calculations,” in Proceedings of the XVIth International Congress on Rheology (ICR '12), J. Maia, I. Emri, and C. Gallegos, Eds., Lisbon, Portugal, August 2012.
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