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A Thermodynamic Investigation of the PVT, Solubility and Surface Tension of Polylactic Acid (PLA)/CO2
Mixtures
by
Syed Hassan Mahmood
A thesis submitted in conformity with the requirements for the degree of Doctor of Philosophy,
Graduate Department of Mechanical & Industrial Engineering, University of Toronto
Copyright by Syed Hassan Mahmood 2012
ii
A Thermodynamic Investigation of the PVT, Solubility, and Surface Tension of Polylactic Acid (PLA)/CO2 Mixtures
Syed Hassan Mahmood
Degree of Master of Science, 2012
Department of Mechanical and Industrial Engineering
University of Toronto
ABSTRACT
This thesis illustrates a comprehensive study on the PVT, solubility and surface tension
properties of polylactic acid (PLA) with dissolved CO2 based on thermodynamic models. The
solubility of CO2 in PLA melt was calculated by means of a gravimetric method, using a
Magnetic Suspension Balance (MSB). The swelling volume of the polymer/gas mixture due to
dissolution of gas was compensated for by direct measurement through a view cell or by
theoretical models such as Simha Somcynsky (SS) - Equation of State (EOS) and Sanchez
Lacombe (SL) - Equation of State (EOS). Three grades of PLA (i.e., PLA3001D, PLA8051D,
and PLA4060D) were chosen. It was observed that the pressure, temperature, D-content and
Molecular weight variance had an effect on the swelling and solubility.
The surface Tension of PLA/CO₂ mixture was also calculated from the captured image
using the Axsymmetric Drop Shape Analysis (ADSA). The effects of varying the pressure,
temperature, and molecular weight on surface tension were investigated.
iii
To the one above for providing me
with an opportunity
To my parents For endless love, support
and encouragement
iv
ACKNOWLEDGEMENTS
I would like to acknowledge the support of my supervisor Prof. Chul B. Park, whose
encouragement and support was second only to that of my parents, without which this research
would not have been possible.
I would also like to thank the members of my Thesis Committee, Prof. Sanjeev
Chandra and Prof. Kamran Behdinan for their invaluable advice and guidance.
My gratitude is extended to the Department of Mechanical and Industrial Engineering
at the University of Toronto for providing the University of Toronto Fellowship. Also, I would
like to thank the members of the Consortium for Cellular and Micro-Cellular Plastics
(CCMCP) for their funding and support in this research.
I would like to thank all my colleagues and fellow researchers formerly and presently
working in the Microcellular Plastics Manufacturing Laboratory for their friendship,
cooperation and support. I am especially thankful to Dr. Gary Li, Dr. Takashi Kuboki, Dr. Nan
Chen, Raymond Chu, Peter Jung, Anson Wong, Lun Howe Mark, Nemat Hossiney, Reza
Nofar and Mohammad M. Hassan for their collaboration on our common research publications
and for the thought-provoking discussions we had during the work. I also want to acknowledge
the contribution of Mohammad M. Hassan and Dr. Guangming Li in the theoretical and
experimental work.
I would also like to thank my parents and all my family members for their endless love,
support and encouragement. Finally, I would like to thank God for providing me with an
opportunity and the patience to grasp that opportunity.
v
TABLE OF CONTENTS
Abstract ........................................................................................................................................ii
Acknowledgements ..................................................................................................................... iv
List of Figures .......................................................................................................................... viii
Nomenclature ............................................................................................................................... x
CHAPTER 1. INTRODUCTION .......................................................................................... 1
1.1 Preamble ............................................................................................................................. 1
1.2 Foam Processing ................................................................................................................. 3
1.2.1 Microcellular Processing ........................................................................................... 3
1.2.2 Physical Blowing Agents........................................................................................... 4
1.2.3 Thesis Objectives and Scope of Research ................................................................. 6
1.2.4 Thesis Structure ......................................................................................................... 7
CHAPTER 2. LITERATURE SURVEY AND THEORETICAL BACKGROUND ........... 8
2.1 Solubility ............................................................................................................................. 8
2.2 Solubility Measurement Methods ..................................................................................... 10
2.2.1 Gravimetric Sorption Technique ............................................................................. 11
2.2.2 Pressure Decay Sorption Technique ........................................................................ 13
2.2.2.1 Previous Research Using Pressure Decay Sorption Technique ....................... 15
2.2.3 Volume Decay Sorption Technique ........................................................................ 16
2.2.4 Piezoelectric Quartz Sorption .................................................................................. 17
2.2.5 In-Line Measurement of Gas Solubility .................................................................. 19
2.2.5.1 In-Line Monitoring ........................................................................................... 19
2.2.5.2 In-Line infrared Sensors ................................................................................... 20
2.2.5.3 Ultrasound ........................................................................................................ 21
2.2.6 Modified Magnetic Suspension Balance Theoretical Treatments ........................... 22
2.3 Theoretical Treatments ..................................................................................................... 26
CHAPTER 3. RESEARCH METHODOLOGY FOR PVT AND SOLUBILITY STUDY 29
3.1 Introduction ....................................................................................................................... 29
3.2 Theoretical Background .................................................................................................... 29
3.3 Methodology and Approach ............................................................................................. 32
3.4 Summary ........................................................................................................................... 34
CHAPTER 4. SOLUBILITY AND SWELLING BEHAVIOR OF PLA IN PRESENCE
OF CO₂………………………………………………………………………………………...35
vi
4.1 Introduction ....................................................................................................................... 35
4.2 Experimental ..................................................................................................................... 36
4.2.1 Materials .................................................................................................................. 36
4.2.2 PVT Data for PLA ................................................................................................... 36
4.3 Solubility of CO₂ in PLA (Binary System)....................................................................... 37
4.3.1 Swelling Behavior of PLA in Presence of CO2 ....................................................... 37
4.3.1.1 Experimental Setup .......................................................................................... 37
4.3.1.2 Experimentation ............................................................................................... 37
4.3.1.3 Pressure and Temperature Effect on Volume Swelling ................................... 38
4.3.1.4 Comparison of the experimentally measured data and Theoretically Predicted
Data ………………………………………………………………………………..40
4.3.1.5 Effect of ‘D’ content/Molecular Weight on volume swelling .......................... 44
4.3.2 Solubility of CO2 in PLA......................................................................................... 45
4.3.2.1 Pressure and Temperature effect on solubility of CO₂ in PLA. ....................... 45
4.3.2.2 Comparison of Theoretical and Experimental Solubility ................................. 48
4.3.2.3 Effect of D-content/Molecular weight on Solubility of CO₂ ........................... 51
4.4 Summary ........................................................................................................................... 53
CHAPTER 5. Surface Tension OF PLA/CO₂ MELT ......................................................... 54
5.1 Introduction ....................................................................................................................... 54
5.2 Experimental Materials ..................................................................................................... 57
5.3 Measurement of Surface Tension of PLA/CO₂ mixture ................................................... 57
5.3.1 Surface Tension of PLA/CO₂ melt .......................................................................... 57
5.3.2 Density determination.............................................................................................. 59
5.3.3 Effects of pressure and temperature variance on surface tension ............................ 62
5.3.4 Effect of Molecular weight on surface tension ........................................................ 65
5.4 Summary ........................................................................................................................... 66
CHAPTER 6. CONCLUSIONS AND FUTURE WORK ................................................... 68
6.1 Summary ........................................................................................................................... 68
6.2 Recommendations and Future Work ................................................................................ 69
References .................................................................................................................................. 70
Appendix .................................................................................................................................... 86
vii
LIST OF TABLES
Table 1: The scaling Parameters for SS-EOS are as following ................................................. 96
Table 2: The scaling Parameters for SL-EOS are as following ................................................. 96
Table 3: Solubility of PLA3001D at 180 °C .............................................................................. 96
Table 4: Solubility of PLA8051D at 180 °C .............................................................................. 97
Table 5: Solubility of PLA4060D at 180 °C .............................................................................. 97
Table 6: Solubility of PLA3001D at 200 °C .............................................................................. 97
Table 7: Solubility of PLA8051D at 200 °C .............................................................................. 98
Table 8: Solubility of PLA8051D at 200 °C .............................................................................. 98
Table 9: Swelling ratio of PLA3001D/CO₂ melt at 180 °C ....................................................... 98
Table 10: Swelling ratio of PLA8051D/CO₂ melt at 180 °C ..................................................... 99
Table 11: Swelling ratio of PLA4060D/CO₂ melt at 180 °C ..................................................... 99
Table 12: Swelling ratio of PLA3001D/CO₂ melt at 200 °C ..................................................... 99
Table 13: Swelling ratio of PLA8051D/CO₂ melt at 200 °C ..................................................... 99
Table 14: Swelling ratio of PLA4060D/CO₂ melt at 200 °C ................................................... 100
viii
LIST OF FIGURES
Figure 2-1 Bubble nucleation inside a die ................................................................................... 9
Figure 2-2: Bubble nucleation inside a mold in injection molding machine: (a) nucleation starts
at gate (generates high cell density); (b) nucleation starts in the mold cavity (generates low cell
density). [14] .............................................................................................................................. 10
Figure 2-3 Details of MSB for density measurement [65] ........................................................ 23
Figure 4-1: Effect of Temperature variance on Swelling Ratio for PLA3001D ........................ 39
Figure 4-2: Effect of Temperature variance on Swelling Ratio for PLA8051D ........................ 39
Figure 4-3: Effect of Temperature variance on Swelling Ratio for PLA4060D ........................ 40
Figure 4-4: Swelling Ratio of PLA3001D at 180 °C with varying pressure ............................. 41
Figure 4-5: Swelling Ratio of PLA8051D at 180 °C with varying pressure ............................. 41
Figure 4-6: Swelling Ratio of PLA4060D at 180 °C with varying pressure ............................. 42
Figure 4-7: Swelling Ratio of PLA3001D at 200 °C with varying pressure ............................. 42
Figure 4-8: Swelling Ratio of PLA8051D at 200 °C with varying pressure ............................. 43
Figure 4-9: Swelling Ratio of PLA4060D at 180 °C with varying pressure ............................. 43
Figure 4-10: Effect of varying D-content/Mw on swelling ratio at 180 °C ............................... 44
Figure 4-11: Effect of varying D-content/Mw on swelling ratio at 200 °C ............................... 45
Figure 4-12: Effect of varying temperature on solubility of PLA3001D .................................. 46
Figure 4-13: Effect of varying temperature on solubility of PLA8051D .................................. 47
Figure 4-14: Effect of varying temperature on solubility of PLA4060D .................................. 47
Figure 4-15: Solubility of Carbon Dioxide in PLA3001D at 180 °C with varying pressure .... 48
Figure 4-16: Solubility of Carbon Dioxide in PLA8051D at 180 °C with varying pressure .... 49
Figure 4-17: Solubility of Carbon Dioxide in PLA4060D at 180 °C with varying pressure .... 49
ix
Figure 4-18: Solubility of Carbon Dioxide in PLA3001D at 200 °C with varying pressure .... 50
Figure 4-19: Solubility of Carbon Dioxide in PLA8051D at 200 °C with varying pressure .... 50
Figure 4-20: Solubility of Carbon Dioxide in PLA4060D at 200 °C with varying pressure .... 51
Figure 4-21: Effect of varying D-content/Mw on Solubility of Carbon Dioxide at 180 °C ...... 52
Figure 4-22: Effect of varying D-content/Mw on Solubility of Carbon Dioxide at 200 °C ...... 52
Figure 5-1: Density difference with pressure change at 180 °C ................................................ 60
Figure 5-2: Density difference with pressure change at 200 °C ................................................ 61
Figure 5-3: Change in surface tension with pressure at 180 °C ................................................. 63
Figure 5-4: Surface tension at various temperature and pressure .............................................. 64
Figure 5-5: Relationship between surface Tension and Solubility ............................................ 65
Figure 5-6: Effect of molecular weight on Surface Tension ...................................................... 66
x
NOMENCLATURE
Ai = Helmholtz energy [J]
CS = Costas and Sanctuary
ci = Chain (molecule) flexibility; 3c is total external degrees o f freedom attributed to
a chain (molecule)
d = Bond length in PCM EOS
EOS = Equation of state
= Molar Gibbs free energy for polymer/gas mixture [J/mol]
H = Enthalpy [J]
h = Plancks constant 6.6260755×10-34
[J.s]
, Bk k = Boltzmann constant 1.380658×10
-23 [J/K]
im = Molar mass of segment (mer) of “i” component [g/mol]
M = Molecular weight of per molecule [g/mol], M = misi
= Avogadro’s number 6.0221367×1023
= Pressure [Pa]
= Characteristic pressure of component “i” [Pa],
** i
i *
i
qzP
sυ
= Reduced pressure */ PP
PCM = Prigogine cell model
PC-
SAFT
= Perturbed Chain Statistical Associating Fluid Theory
= The number of nearest neighbor sites per chain-like molecule (s-mer), si(z - 2)+2.
= Dimensionless identity for SS-EOS
= The combinatorial factor for PCM
r = Number of mer per molecule, **
*
ρRT
MPr
= Gas constant 8.3143 [J/(mol·K)]
S = Entropy [J/K]
xi
SAFT = Statistical Associating Fluid Theory
= Number of mers per molecule of component “i”
SL = Sanchez–Lacombe
SS = Simha–Somcynsky
= Volume swelling ratio
T = Temperature [K]
*
iT = Characteristic temperature of component “i” [K], ii
B
qzT
ck
= Reduced temperature */TT
*
iυ = Characteristic volume per mer of component “i” [m3/mer]
*
iV = Characteristic volume of component “i” (m3/mol)
= Reduced volume,
ix = Mole fraction of “i” component in mixture system
X = Solubility (g-gas/g-polymer)
y = Occupied lattice site fraction
Z = 12, the lattice coordination number
i * = Characteristic energy per mer of component “i” (J/mer)
= dimensionless number for SS-EOS
1 = Volume fraction of gas in mixture system
2 = Volume fraction of polymer in mixture system
G
1 = Chemical potential of gas in vapor phase [J/mol]
P
1 = Chemical potential gas in the polymer melt [J/mol]
* = Characteristic density of bulk material [g/cm3]
Λ
= de Broglie wavelength
= Flexibility parameter
= Lattice-site volume
Γ = PCM geometrical constant
xii
~ = Reduced density V
~/1
Subscripts
1 = Indicates gas
2 = Indicates polymer
i = Indicates component number or component in x-direction
j = Indicates component number in y-direction
F = Indicates foam
G, g = Indicates gas
Superscripts
G, g = Indicates gas or vapor
P, p = Indicates polymer
1
CHAPTER 1. INTRODUCTION
1.1 Preamble
Foamed plastics surround us in the shape of different commodities every day. This is a
testament to the extent that foamed polymeric materials have pervaded our everyday life.
Foamed polymeric material can be classified as either a thermoplastic or thermoset foam.
Thermoplastic foams are recyclable, whereas thermoset foams cannot be reprocessed because
it’s extensive crosslinking. The applications of the foamed product dictate the density of the
final product; consequently, several types of polymeric materials are foamed to various low
densities for applications that require attributes such as weight reduction, insulation, buoyancy,
energy dissipation, convenience, and comfort.
Thermoplastic and thermoset foam products differ from solid plastic products and are
identifiable by virtue of a unique cellular structure. The latter is obtained by the atmospheric
expansion of a blowing agent in the polymer matrix. This cellular structure is normally
characterized in terms of the cell density and cell size. For conventional foams, typical cell
population densities are within the range of 10³-10⁶ cells/cm³, with cell sizes of the order of
100 μm or larger. However, the cell size and distribution can be inconsistent, hence
compromising the mechanical properties of the foam. Conversely, microcellular plastics are
characterized by cell densities greater than 10⁹ cells/cm³ and cell sizes smaller than 10 μm.
This group of plastic foams was conceived by Masrtini et al. [1], and is based on the notion
that if a large number of bubbles smaller than the pre-existing flaws in the polymer are created,
the material cost can be reduced without compromising mechanical properties. It has been
2
observed that microcellular plastics possess superior impact strength [1], toughness [2], and
fatigue life [3] compared to solid polymers.
Furthermore, solid polymeric foams may possess either closed or open cells; closed
cell foams possess a cellular structure in which neighboring air bubbles are entrapped in a
continuous macromolecular phase. Open cell foams, on the other hand, have a cellular network
in which continuous channels are available throughout the solid macromolecular phase.
The gaseous phase in any polymeric foam material is obtained using blowing agents in the
foam manufacturing process. There are generally two types of blowing agents used in foam
production: chemical blowing agents and physical blowing agents. Chemical blowing agents
are chemical compounds which evolve gases under foam processing conditions through
thermal degradation or chemical reactions. Physical blowing agents, on the other hand, are
inert gases, such as nitrogen and carbon dioxide; volatile hydrocarbons such as propane, n-
butane, i-pentane; and low boiling point chlorofluorocarbons (CFCs), hydrofluorocarbons
(HFCs), and hydrochlorofluoro-carbons (HCFCs).
Due to the environmental hazard posed by CFCs and HCFCs, there has been a drive to
replace these blowing agents with more environmentally friendly substitutes. The properties of
blowing agents and their impact on the processing variables in foam production are essential
issues that must be considered in order to find effective replacements. The specific
thermodynamic and kinetic properties that have the greatest influence on the ability to produce
microcellular foams are the solubility and diffusivity of the blowing agent in the polymers.
The solubility determines the amount of blowing agent that can be absorbed by the polymer at
any given temperature and pressure, while the diffusivity determines both the rate at which the
blowing agent will penetrate into the polymer matrix to form a homogeneous solution, as well
3
as the rate at which the blowing agent escapes to the atmosphere during cell nucleation and
growth processes.
1.2 Foam Processing
1.2.1 Microcellular Processing
The foamed plastics industry is continuously developing, which encompasses various
methods of production for many product applications. The choice of polymer, blowing agent,
and production method dictates the foam formation and its morphology; therefore, its
properties, stemming from an industrial challenge to enhance polymer value by improving
performance/weight characteristics. Earlier work focused on batch processes; the concepts
resulted in good foam structures with cell sizes less than 5 μm using supercritical carbon
dioxide [1]. The batch process was further developed and improved by Cha et al. [4]; whereas
Kumar [5] and Kumar and Suh [6, 7] developed a semi-continuous process derived from a
modified thermoforming process. Further investigation by Park [8], Park et al. [9], and Park
and Suh [10] led to the development of an extrusion-based process for a microcellular filament
as the first step in the development of a continuous process.
The fundamental principle involved in the formation of microcellular polymer foams
consists of three basics steps: 1) polymer/blowing agent solution formation; 2) microcellular
nucleation; and 3) cell growth and density reduction. The single-phase polymer/blowing agent
solution in the first step are formed by saturating the polymer with the blowing agent under
high pressure. The saturation point is determined by the solubility limit of the blowing agent in
the polymer, while the time required for the solution formation is determined by the rate of
diffusion of the blowing agent into the polymer matrix.
4
Microcellular nucleation is achieved by inducing a thermodynamic instability in the
single-phase solution. This is usually accompanied by drastically reducing the solubility of the
gas in solution by controlling the pressure and/or temperature of the solution [11-13]. Since the
separation of the polymer and gas phases is thermodynamically more favorable, the resulting
supersaturated mixture becomes the driving force for the nucleation of numerous microcells
[1]. Continuous microcellular processing typically utilizes a rapid pressure drop to nucleate
bubbles. This stage is very crucial to the overall process, because it dictates the cell
morphology of the material and its resulting properties. Therefore, solubility as a function of
pressure is important for the development of the process.
The final stage in the production of microcellular plastics is cell growth. After cell
nucleation has occurred, any available gas diffuses into the cell and increases the cell size,
thereby reducing the density of the polymer matrix. Generally, cell growth is affected by the
time allowed for the cells to grow, the system temperature, the amount of gas available (state
of super saturation), the processing pressure, and the viscoelastic properties of the polymer/gas
solution [14].
1.2.2 Physical Blowing Agents
An important aspect of the creation of a cellular structure is the use of a physical
blowing agent. Historically, CGCs and HDCs, such as CFC-11 and HCFC-141b, were used
primarily for low density foam production mainly because of their solubility, volatility, and
non-toxic nature; however, their stability and reactivity with ozone in the atmosphere raised
substantial concern about ozone depletion. In an effort to address the environmental impact of
these man-made compounds, the Montreal Protocol [15] was signed in 1989 by 29 countries
and amended in subsequent years. The Montreal Protocol mandates the gradual phase-out of
5
the production of CFCs by 2010 and HCFCs by 2030 undeveloped countries. As a result, CFC
production fell from 980 metric tons in 1986 to 95 metric tons in 1996 [16]. Since the early
1990s, global warning or the greenhouse effect has become another major issue. The
Intergovernmental Panel on Climate Change (IPCC) reported a scientific assessment on the
warming potential of various compounds relative to carbon dioxide [17]. It was reported that
the global warming potential of CFCs and HXFXs is 5,000-10,000 times greater than that of
carbon dioxide with stratospheric life cycles of 60-130 years. In addition, the Kyoto Protocol
on Climate Change [18] adopted by 160 nations in 1997, sets binding limits on greenhouse gas
emissions for developed countries. It strengthens the framework established by the Montreal
Protocol with new policies and measures.
The combined global warming and ozone depleting potential of these substances, as
well as the resulting policies, have created a void in the foam processing industry; the need
has, therefore, arisen to replace CFCs and HCFCs with environmentally friendly blowing
agents possessing good foam-blowing properties. The concern over the ozone layer and global
warming represent just a few of the issues facing the foam processing industry. Disposal,
waste stream control, and usage of recycled plastics still require a deep understanding of
foaming technology.
Microcellular plastics do not utilize the conventional CFC foam blowing agents;
instead, carbon dioxide and nitrogen are typically used. Although these blowing agents
represent a dramatic improvement in terms of environmental hazard, they, too, pose their own
difficulties. Carbon dioxide has a high solubility in the plastic melt, approximately 10% at 200
°C and 27.6 MPa [19], and produces a very uniform cell structure. Conversely, nitrogen has a
lower solubility, about 2-3% at 200 °C and 27.6 MPa, and processing requires a much higher
pressure to dissolve sufficient nitrogen to create a uniform structure as explained in Section
6
1.2.1. Higher processing, however, requires more robust processing equipment and leads to
higher equipment and processing costs. Other alternative blowing agents used are liquid
blowing agents such as butane and iso-pentane. To date, however, liquid blowing agents have
not been successfully used to achieve a microcellular structure. One possible barrier that exists
with the use of these liquid blowing agents is the lack of information about their solubility and
diffusivity.
1.2.3 Thesis Objectives and Scope of Research
Since the solubility of blowing agents in polymer melts plays a key role in the plastic
foaming processing, this research was focused on the following aspects:
i. To propose technically sound experimental approaches and thermodynamic
models for the PVT, solubility and surface tension investigation of polymer/gas
mixture (binary).
ii. To obtain reliable (more accurate) PVT, solubility data, surface tension and
thermodynamic properties of polymer/blowing agents by systematic
investigation
iii. To verify the accuracy of solubility data determined by using various EOSs
and correct them with the help of a visualization system.
iv. To determine the effect of D-content/Mw on the solubility, surface tension and
swelling of the PLA/gas mixture.
7
1.2.4 Thesis Structure
This section provides a brief overview of the present thesis.
Chapter 2 explores the literature review on the thermodynamic study of the phase equilibrium
in a polymer system and gas solubility in polymer melts. The various methods available to
measure the solubility and diffusivity of blowing agents in polymer are examined. Theoretical
methods to predict the solubility is discussed as well.
Chapter 3 introduces the general research methodologies for the study of PVT and solubility
behavior of polymers. It was found that there are some deviations existing among the
thermodynamic models in terms of theoretical solubility and swollen volume prediction. As a
result, further investigation was done to verify the equation of states (EOSs).
Chapter 4 introduces the study of PVT and the solubility behavior of polymers/gas (binary
system). The solubility of CO2 in polymer was determined by using experimental data. The
visualization system was used to obtain the swelling behavior of the polymer/gas mixture. The
obtained data is then compared with the theoretical data obtained by means of EOS, namely
SS-EOS and SL-EOS.
Chapter 5 encompasses the measurement of the surface tension of the PLA/CO₂. Effect on the
interfacial tension with the variance in pressure, temperature, molecular weight, and D-content
is investigated. SS-EOS is used to obtain theoretical density of the PLA/CO₂ and was
compared to the experimentally obtained data.
Chapter 6 provides a summary, as well as conclusions of the research. Recommendations for
future work are also presented in Chapter 6.
8
CHAPTER 2. LITERATURE SURVEY AND THEORETICAL
BACKGROUND
2.1 Solubility
Solubility is defined as the amount of physical blowing agent (PBA) that can be
dissolved into a unit mass of polymer at a particular temperature and pressure (where the unit
is g-PBA/g-Polymer). The solubility is not only a critically important parameter for fabricating
plastic foams, but also an important property in developing blowing agents (BAs) and
evaluating their performances.
For effective process design, the system pressure must be high enough to dissolve all of
the injected gas into the polymer melt. When the polymer/gas solution exits the extrusion die,
the pressure will drop dramatically; this will initiate the bubble nucleation. The bubbles’
nucleation stage is crucial in the plastic foaming process due to the formation of a
microcellular structure. Theoretically, cell nucleation occurs when the pressure of the
polymer/gas mixture drops below the solubility pressure (or threshold pressure [20] to be
exact), as shown in Fig. 2.1 The cell nucleation mechanism has been described in detail by lot
of researchers [21-25], where the nucleation rate was governed by the degree of super
saturation, i.e., a metastable state determined by the saturation or solubility information.
9
Figure 2-1 Bubble nucleation inside a die
Blander and Katz [21-23] have reviewed the classical nucleation theory to estimate the
rates of bubble nucleation in pure liquids. The work of formation, W, for a spherical bubble of
radius, R, is shown in equation 1-2:
2-1
where is the surface tension; is the pressure of the bubble at the moment it is formed,
which is typically determined as a saturation pressure in a pure component system or solubility
pressure corresponding to the amount of dissolved gas in the mixture system; is the pressure
of the system; n is the number of bubbles; and are the chemical potentials of the
new and old phase, respectively. Hence, the solubility pressure information is required for the
calculation of the nucleation point and nucleation rate. Also, to study surface tension of the
polymer/gas mixture, solubility information is a prerequisite. For this reason, the solubility of
gases in a polymer melt during the plastic foam processing condition has been of great interest
to foaming manufacturers and researchers.
Solubility information also plays a very important role in foaming with an injection
molding machine. In our group, Lee et al. [26] found the cavity pressure of a foaming mold
10
has a significant influence on cell nucleation (Fig. 2.2). He claimed that if the cavity pressure
is lower than the solubility pressure (or the threshold pressure [20]) of the injected gas and if
the pressure before the gate is high enough, cell nucleation occurs at the gate with a high
pressure drop rate. In such cases, the cell density will be high. However, if the cavity pressure
is higher than the solubility pressure (or the threshold pressure), cell nucleation occurs along
the mold cavity with a low pressure drop rate, resulting in a low cell density.
(a) (b)
Figure 2-2: Bubble nucleation inside a mold in injection molding machine: (a) nucleation
starts at gate (generates high cell density); (b) nucleation starts in the mold cavity (generates
low cell density). [14]
2.2 Solubility Measurement Methods
There are two experimental techniques, known as permeation and sorption that can be
used to determine the solubility of a gas in a polymer. Permeation experiments involve
measurements of the steady state mass flow of a gas flowing through a thin membrane;
11
whereas in the sorption kinetics techniques, the mass uptake of gas by the polymer sample is
measured. The major difference between the two techniques is in the method by which
solubility is determined. Permeation experiments rely primarily on a mathematical expression
to determine the permeability, diffusivity, and hence the equilibrium solubility of the gas in the
polymer indirectly when steady state flow has been attained. The sorption method, on the other
hand, directly measures the mass gain of the polymer due to gas dissolution and, therefore,
represents a more direct approach to determining the equilibrium solubility. The sorption
method will be employed in this thesis to determine the solubility information for polymer-
blowing agent combinations, and hence this section will focus only on a review of sorption
techniques.
2.2.1 Gravimetric Sorption Technique
The gravimetric sorption method measures the solubility by simply measuring the mass
gain of a polymer sample due to gas dissolution. One of the earliest gravimetric techniques
utilized the quartz spring measuring system known as the McBain Balance [27]. The balance
was operated by suspending the polymer from a quartz spring in a low pressure gas
environment. As the polymer gained weight due to gas dissolution, the spring elongated.
Utilizing Hooke’s Law, the mass of the sample can be determined as a function of elongation
by calibrating the spring with known weight increments. The quartz spring method was used,
for example, to determine the solubility data of ethylbenzene [28] and toluene [29] in
polystyrene at various vapor pressures.
Batch process, a high pressure gravimetric technique, was utilized by Baldwin et al.
[30] for the measurement of carbon dioxide solubility and diffusivity in thermoplastic
polyesters. This process utilizes multiple samples, which are exposed to the gas for various
12
time periods, and compiles the mass uptake curve by normalizing the time axis for sample
thickness.
An in situ gravimetric sorption method directly measures the solubility by measuring
the mass gain of the polymer with a high-precision electro balance capable of measurements at
high temperatures and pressures. The sensitivity of the instrumentation, which can attain
values of 1 ppm (part per million), makes the technique desirable for solubility measurement
involving low solubility gases such as inert gases. This method is also suitable for the
measurement of solubility for polymers in either the rubbery or glassy state. The apparatus is
mounted on a vibration-free surface with the weighing unit contained in a constant temperature
environment.
The solubility of the blowing agent is determined from measurements of the increased
mass of the sample with increasing blowing agent pressure. Wong et al. [31] reported on the
use of an electronic microbalance to measure the gas solubility and diffusivity of carbon
dioxide and HFC134a in PS, filled poly (vinyl chloride) -FPVC, and unplasticized poly (vinyl
chloride) UPVC.
An alternative method for measuring gas solubility in polymers was presented by
Chaudhary and Johns [32]. It involved using a magnetic suspension device similar to the
electro balance. The most significant difference is that the weighing mechanism is physically
decoupled from the high temperature and high pressure environments through a magnetic
suspension coupling. This equipment was used to measure the solubilities of nitrogen,
isobutane, and carbon dioxide in polyethylene. More recently, Sato et al. [33] reported on the
use of a magnetic suspension balance to measure the solubilities of carbon dioxide in
poly(vinyl acetate) (PVAc) and polystyrene.
13
The high sensitivity of these types of balances dictates that mass measurements must
be corrected to accommodate for the change in buoyancy of the sample. Therefore, knowledge
of the dilation of the polymer with blowing agent uptake is also required for the solubility
calculations.
2.2.2 Pressure Decay Sorption Technique
The pressure decay technique is used to determine the solubility of gas in a closed
system by measuring the pressure decrease due to gas dissolution in the polymer sample. This
method relies on the assumption that all changes in the gas pressure are due to mass sorption
of the polymer. Consequently, the mass uptake of the polymer is determined indirectly by
measuring the pressure decay of the fixed volume system. By measuring the apparatus volume
accurately and recording the temperature and pressure of the system, the mass of the gas in
closed system is determined as a function of time using its equation of state. The solubility is
then determined from the overall experimental pressure change. This technique requires
careful calibrations and can be used only for gases whose equations of state are accurately
known. The three methods used for employing the pressure decay technique are single-, dual-,
and three-chamber systems.
Single-Chamber Sorption: The single-chamber system [34-37, 11-12] consists of a single
chamber containing the polymer sample. The chamber is subjected to a rapid pressure
increase, and the resulting pressure decay due to sorption is recorded as a function of time.
Due to rapid mass gain in initial stages and the thermodynamics of the gas system, a stable
reading is often not recorded until the pressure reading (needed to determine the initial mass of
gas in the system) is extrapolated from the pressure decay curve. The extrapolation, however,
14
can cause a significant error in determining the initial mass of gas present in the system, and
the corresponding total mass change due to gas sorption in the polymer.
Dual-Chamber Sorption: The dual-chamber sorption system [13, 38] uses a reservoir chamber
of known volume, filled with gas at a known pressure, while another chamber contains the
polymer sample. By opening a valve separating both chambers, the gas is allowed to flow into
the second chamber and, therefore, into the polymer. The valve is then closed and the sorption
chamber is observed for pressure decay. The reservoir chamber pressure is also measured. The
mass absorbed by the polymer sample is then determined based on the difference of the initial
mass of gas in the reservoir chamber and the final mass of gas in both the reservoir and
sorption chambers.
Sorption experiments are usually performed in a stepwise manner in order to make sure
the pressure drop for each experimental pressure step is relatively small. A typical pressure
decay sorption experiment begins with a low reservoir and corresponding low sorption
pressure. The resulting pressure decay due to sorption is observed until the equilibrium
pressure indicates that equilibrium mass gain has occurred. New gas is introduced into the
system without evacuating the chambers so that the pressure is increased by a step amount.
The pressure decay is then monitored, and the process is repeated. The solubility is determined
as a function of pressure by successively adding the mass gain of each pressure.
Three-Chamber Sorption: The three-chamber system [39,40] uses the measurement principle
identical to the dual-chamber configuration described above; that is, the mass uptake of the
polymer is determined from the equation of state of the gas, using measurements of chamber
volume, gas pressure, and gas temperature. The three-chamber system consists of two
reservoir chambers: the first reservoir is used as a pressure source for the sorption chamber;
while the other is used as a source for the first reservoir. This configuration allows for multiple
15
measurements at different pressures without introducing new gas and a new sample. This
method minimizes the temperature shock to the system caused by the introduction of gas.
2.2.2.1 Previous Research Using Pressure Decay Sorption Technique
Nevitt and Weale [13] were responsible for some of the earliest measurements of gas
solubilities in polymers using the dual-chamber system. They reported on the solubility of
hydrogen and nitrogen in polystyrene over the pressure of 8.1-30.4 MPa, and at elevated
temperatures up to 190 °C. High pressure was achieved in the reservoir chamber by using a
mercury pump. The pressure in the sorption chamber was measured one minute after first
subjecting the sample to the high-pressure gas. This delay in measurement was a result of the
pressure instability produced by the initial expansion of gas into the sorption chamber; this
was further compounded since the gas was not pre-heated to match the temperature of the
sorption chamber.
The unstable pressure observed initially contributed to the difficulty experienced in
determining the initial pressure reading required to calculate the equilibrium solubility. To
reduce the magnitude of this error, the researchers employed a large sample of 40-100 grams,
which was cut into thin strips to increase the mass diffusion rate (or reduce the time required to
obtain equilibrium stability), and thus increase the magnitude of the pressure drop. Utilizing
the stepwise sorption technique described earlier, the solubility was then calculated as a
function of pressure.
Lundberg et al. [34,35] and Lundberg [36] used a single-chamber sorption apparatus to
determine the solubility of gases in polymers at pressures between 3 and 71 MPa, and
temperatures between 102 and 188 °C. The stepwise sorption experiment was used to estimate
the solubility and diffusivity of a gas in a molten polymer.
16
Durril [37] and Durril and Griskey [11,12] employed a pressure decay method with a
single-chamber apparatus to investigate the solubility and diffusivity coefficients of nitrogen,
helium, carbon dioxide, and argon in molten polyethylene, polyisobutylene, and
polypropylene, at pressures up to 2 MPa. Before coming into contact with the sample, the test
gas was preheated in a thermostatted air environment. The first pressure reading, however, was
not reduced until 100 seconds after the gas first contacted the polymer sample. A stepwise
sorption methodology was used to calculate the solubility as a function of pressure.
Other researchers have utilized the pressure decay method to only measure the
solubility characteristics of gases in polymers at pressures up to 2 MPa [41-43] and 8.3 MPa
[44]. Stern and De Meringo [38] used a dual-chamber system to measure the solubility of
carbon dioxide in cellulose acetate at pressures up to 4.6 MPa.
Sato et al. [39] employed a three-chamber sorption apparatus to measure the
solubilities of carbon dioxide and nitrogen in polystyrene for pressures up to 20 MPa, and
temperatures in the range of 100-180 °C. The sorption chambers were controlled to within
0.05 K by a constant temperature air bath. In a later publication, Sato et al. [40] reported on the
solubility of carbon dioxide and nitrogen in polypropylene, high-density polyethylene, and
polystyrene. PVT measurements of the polymer at high temperatures and pressures were
conducted to provide the volume of polymer necessary for the solubility calculations, while
the swollen polymer volumes, caused by gas dissolution at different pressures and
temperatures, were predicted using the Sanchez Lacombe Equation of State [45-47].
2.2.3 Volume Decay Sorption Technique
As the name implies, volume decay sorption techniques measure the volume change of
the gas due to polymer sorption in a closed system at constant pressure and temperature. The
17
mass uptake of the polymer, or essentially the solubility, is indirectly determined from
measurements of the volume decay.
A volume decay sorption apparatus was utilized by Rosen [48] to measure the
solubility and diffusivity of acetone in cellulose acetate, methyl chloride vapor in polystyrene,
and water vapor in neoprene, at sub-atmospheric pressures. The system was designed as an
alternative to the quartz spring apparatus.
Mulrooney [49] used a constant pressure sorption concept based on the volume decay
method to investigate the solubility and diffusivity of liquid blowing agents such as isopentane
in polystyrene at elevated pressures. A positive displacement syringe pump capable of
operating in a constant pressure mode was used as the constant pressure source, while the
entire assembly was operated in a thermostatted air bath for constant temperature control. The
reasoning was that since the system was closed, any volume changes occurring in the blowing
agent were correlated to the piston movement of the pump and electronically recorded.
However, the swelling effect of the polymer could not be accounted for. If the volume
increased equally as the volume of isopentane decreased, then no net change in volume would
be observed. However, if the volume change of the isopentane was less than the volume
change of the sample, the net measured volume change would be underestimated.
2.2.4 Piezoelectric Quartz Sorption
Piezoelectric quartz sorption is a technique which measures solubility based on the
principle that the vibration frequency of a quartz crystal changes in response to a change in the
mass deposited on the crystal surface. This technique is usually applied to organic solvents.
There are two main components in this experimental set up: a sorption cell containing
the polymer coated with the piezoelectric crystal oscillator, and a solvent cell containing the
18
gas. When gas is introduced into the sorption cell, it is adsorbed onto the polymer. This, in
turn, changes the frequency of the crystal oscillator, which is measured with a frequency
detector, recorded, and indicated on a frequency counter. Also, this experiment incorporates a
few other variables that could lead to a frequency change, which include the following: the
sorption of gas into the polymer, adsorption of gas onto the crystal, coating of polymer film,
hydrostatic pressure of ideal gas, and viscous resistance of the gas.
Bonner and Cheng [50, 51] experimentally determined that the frequency of a quartz
crystal oscillator do vary with temperature and pressure. Hence, in order to account for the
pressure dependence of the frequency in their sorption measurements, two crystal oscillators
with similar pressure dependencies are used. One of the sorption crystals is coated with the
polymer, while the other uncoated crystal oscillator is used as a reference crystal. In a situation
when a reference crystal is not used, an accurate estimate of the pressure dependence of the
crystal oscillator at the experimental temperature would be needed. Such an estimate has been
reported by Stockbridge [52] for pressures below 0.13MPa.
By using the experimental technique with the uncoated reference crystal, Masuoka et
al. [53] investigated the solubilities of benzene, cyclohexane, n-hexane, toluene, and
ethylbenzene in polyisobtylene at low temperatures up to 65 °C and low pressures. The effect
of polymer coating thickness (in the range of about 0.2-1.4 µm) on the solubility of the solvent
in the polymer is tested, and they found that the experimental results were not affected within
this range. On top of that, they also concluded that the molecular weight had no definitive
effect on the solubility for polymer molecular weights of 50,000 and 100,000. In an
experiment dispensing with the reference crystal, Wang et al. [54] experimentally determined
the pressure dependence of the crystal oscillator without a polymer coating at pressures up to
10 MPa in an atmosphere of helium.
19
2.2.5 In-Line Measurement of Gas Solubility
In-line measurement techniques were developed from an interest in determining phase
equilibria during the actual foaming process. Usually, these techniques would incorporate the
measurement devices in-line with the foaming process. Phase separation, or the solubility
limit, is then detected by means of sensitive instrumentation or visually.
2.2.5.1 In-Line Monitoring
Dey et al. [55] and Zhang et al. [56, 57] reported an in-line technique for measuring the
gas solubility in various polymers during the foam extrusion process. The apparatus for this
technique consisted of an extruder with a specially designed optical window, and the flow
restrictor valve positioned between the die and the end of the extruder. Through this window,
the occurrence of bubble formation could be observed using a microscope-CCD camera-
monitor/ recorder system.
In order to detect the appearance or disappearance of bubbles during phase separation,
a two-phase, polymer-gas mixture was created by initially using a low pressure in the optical
window. The pressure was then gradually increased so that the polymer and gas became a
single-phase solution. This pressure was taken to be the lowest pressure required to keep the
gas in the solution under specified conditions. Lastly, the solubility was calculated by
combining this information with the gas flow rate and the melt throughput.
The parameters affecting the in-line measurement of gas solubility was found to be the
degree of mixing (single- or twin-screw extruder), the screw rotational speed, and polymer
throughput. One reported advantage of this in-line technique was that the solubility data could
be recorded in real-time, and therefore, could account for the dynamic nature of the extrusion
20
process, the possible role played by the extrusion process in gas dissolution, and bubble
nucleation in the melt.
2.2.5.2 In-Line Infrared Sensors
Near infrared (NIR) spectroscopy is a technique for monitoring the polymer/blowing
agent mixture during polymeric extrusion foaming processes. Through the use of dual-
transmission infrared sensors or probes, which transmit NIR light through the polymer running
in a flow cell, infrared monitoring of the process is achieved. The probes are linked with fibre-
optic cables to a Fourier transform near-infrared spectrometer (FT-NIR), which records the
absorption spectra of the melt. The flow cell for NIR measurements is located at the exit of the
extruder on a side stream of polymer flow taken from the main flow stream. Downstream of
the flow cell, a gear pump is installed to realize a steady flow rate.
NIR spectroscopy has been reported to have plenty of advantages, such as remote data
collection and ease of sample handling. It has also been used for the online measurements of
polymer composition [58], polymer viscosity [59], and concentration of HCFC in polystyrene
[60].
For instance, on-line NIR spectroscopy was utilized by Nagata et al. [61] in measuring
the Carbon Dioxide (CO2) concentration in molten propylene for CO2 extrusion foaming
processes. Three different CO2 concentrations and three separate flow rates were used
experimentally. In order to remove the baseline of the obtained NIR spectra, the wavelet
transform was employed (the given signals were represented by the linear combinations of
known functions). They claimed that experiments demonstrated a strong correlation between
the NIR spectrum and the CO2 raw NIR spectrum; the effects of temperature and flow rate
were erased. This technique, however, is limited in practice, since the incident light from the
21
probes would be scattered out if any dispersed material is present in relatively large quantities
in the melt. The absorbance may then become too weak to be analyzed precisely. Furthermore,
the calibration curve must be developed whenever the polymer and/or the processing
conditions are changed.
Thomas et al. [60] also investigated the ability of NIR spectroscopy to detect bubble
formation in the die as a function of blowing agent concentration and pressure for the
PS/HCFC 142b system. When the die pressure was gradually decreased, they observed that
NIR sensors could detect degassing of the melt. The appearance of bubbles caused scattering
of the light, which induced a large increase in attenuation at the level of baseline absorbance of
infrared waves. They also investigated the effect of talc on the performance of NIR
spectroscopy, and found that NIR analyses were still possible for talc contents
22
(A1, A2, A3, …) that are detected by the receiving transducer. From the thickness, e (m), and
the time delay between successive echoes, ∆t (s), the sound velocity, v (ms-1
), is determined
using the following relation:
2-2
On the other hand, the attenuation, a (dB/cm), is obtained through the relative amplitude of
successive echoes:
2-3
Sahnoune et al. employed these techniques [63] to measure the thermodynamic
properties of polystyrene/HCFC 142b mixtures. For phase separation measurements, they
observed that the velocity of sound decreased by as much as 4.5% from a steady state value as
the pressure was decreased. This was explained to be due to the phase separation process. The
attenuation, on the other hand, exhibited a different trend in relation to the thermodynamics
state of the blowing agent.
2.2.6 Modified Magnetic Suspension Balance Theoretical Treatments
Masahiro Ohshima and his coworkers [65] tried to measure the solubility of gas in
polymer by modifying the MSB. The densities of two polymer/CO2 single-phase solutions,
poly(ethylene glycol) (PEG)/CO2 and polyethylene (PE)/CO2, were measured at temperatures
higher than the melting temperature of a polymer under CO2 pressures in the range of 0-15
MPa using a newly-proposed gravimetric method. A magnetic suspension balance (MSB) was
used for the density measurement under the high pressure CO2. A thin, disc-shaped platinum
23
plate was submerged in the polymer/CO2 single-phase solution in the MSB high-pressure cell.
The weight of the plate was measured while keeping CO2 pressure and temperature in the
sorption cell at a specified level. Since the buoyancy force exerted on the plate by the
polymer/CO2 solution reduced the apparent weight of the plate, the density of the
polymer/CO2 solution could be calculated by subtracting the true weight of the plate from its
measured weight. Experimental results showed that the density of PE/CO2 solution increased
with the increase of CO2 pressure; and the density of PEG/CO2 solution decreased with the
increase of CO2 pressure. To differentiate the effect of CO2 dissolution in polymer from that of
mechanical pressure, the density of polymer/CO2 solution was compared with the density of
neat polymer under the given mechanical pressure, which was calculated using the Sanchez-
Lacombe equation of state and Pressure-Volume-Temperature (PVT) data of the polymer. The
comparison could elucidate that the dissolution of CO2 in the polymer-reduced densities of
both PEG/CO2 and PE/CO2 systems. However, this was not the case; the degree of CO2
induced-density reduction was different between the two polymer/CO2 systems.
Figure 2-3 Details of MSB for density measurement [65]
24
When the platinum plate is submerged in polymer/CO2 solution, the measured weight
of the plate becomes smaller than the true weight of the plate due to a buoyancy force exerted
on the plate by the polymer/CO2 solution. The buoyancy force is equal to the weight of
polymer/CO2 solution displaced by the plate, and it is calculated by multiplying the plate
volume by the density of polymer/CO2 solution. Therefore, knowing the volume and mass of
the plate a priori, the density of polymer/CO2 solution can be calculated from the buoyancy
force or the apparent weight of the platinum plate.
The force balance equation around the plate and the wire is expressed by
2-4
where and are the density of polymer/CO2 solution and CO2, respectively;
is the readout value of the apparent total weight of the plate, wire, and
measuring load hook at the experimental temperature, T, and CO2 pressure, P, condition;
is the apparent total weight of the plate, wire and measuring load hook at a reference
temperature and pressure condition; and are the volume of the platinum plate and that of
the wire, respectively; is the volume of measuring load hook; is the volume fraction of
the wire submerged in the solution; d is diameter of the wire connecting the platinum plate to
the measuring load hook; c is surface tension of polymer/CO2; h is contact angle between the
wire and the polymer/CO2 solution as shown in Figure 2-3(b); g is the gravitational constant.
The subscript i, for example di and Vw,i in Figure 2-3(b), indicates that it is the value in the
case of using the i-th wire.
Considering that the plate and wire were both made of platinum, the temperature and
pressure corrections of the volumes, V and Vw, were made using Eq. (2.5):
25
2-5
where Vref and Vw,ref are reference volumes of platinum plate and wire; m and E are Poisson’s
ratio and Young’s modulus of the platinum, respectively. They are given by 0.38 and 1.68
MPa, respectively. ζ is the coefficient of thermal expansion, which is 9.1x 10-6
K-1
.
The surface tension of polymer/CO2, g, and contact angle, u, were unknown and no
literature value was available. To eliminate g and u from the balance equation, two wires in
different diameter, d1 and d2, were used. The density measurements were conducted using each
wire individually at the same temperature and pressure.
Assuming that the two wires have the same surface tension, c, and contact angle, h, against the
polymer, we get the following:
2-6
Thus, the density of polymer/CO2, is given by the following:
2
-
7
26
2.3 Theoretical Treatments
There are theoretical approaches for explaining and predicting the solubility of gas in a
polymer. These theories are initially devised from the prediction of the pressure-volume-
temperature relationship for a pure component. They are then expanded to polymer/solute
systems. The models presented are based on a lattice fluid model in which each molecule
occupies r sites (an r-mer) with vacant sites present. It is assumed that there are random
mixings of r-mers with each other and with the vacant sites. These theoretical models, which
are summarized and presented in this thesis, are the Flory-Huggins theory [66, 67], Sanchez-
Lacombe Equation of State (SL-EOS) [45-47], and the Simha-Somcynsky Equation of State
(SS-EOS) [68].
The Flory-Huggins (F-H) theory [66, 67] was derived from considering the polymer
solution as a lattice in which a solvent molecule occupies the same lattice position as the
polymer segment. It gives information about the solubility and phase relationships, and
assumes that the volume and enthalpy of mixing are zero. This introduces a reduced Gibbs
energy parameter, x, to correct the energetic effect of mixing. The x-parameter is taken to be
independent of composition and temperature. The original F-H theory was modified by Blanks
and Prausnitz [69], who introduced an entropic contribution to the x-parameter. Nevertheless,
even though the theory is modified, the F-H theory is still considered inadequate for describing
polymer solutions. This is because it ignores the equation of state properties of pure
components and the effect of polymer chain architecture on intermolecular packing.
The Sanchez and Lacombe Equation of State (S-L EOS) [45-47] is a lattice fluid model
for pure fluids and mixtures. It requires three pure component parameters to characterize a
pure fluid and one adjustable binary interaction parameter. When the PVT properties of the
components at the solubility pressure are acquired, the equilibrium solubility of gas dissolved
27
into a polymer can also be determined. However, one complication that might arise is that
there is scarce information on the PVT properties of polymers and interaction parameters. If
the solubility data is available in a limited range, one can use non-linear regression analysis to
determine the parameters.
Panayiotou and Verra (P-V) [70] also obtained an equation of state based on a lattice
hole theory. The difference between this theory and the S-L EOS is that a constant site volume
for all r-mers is used, and non-random mixing arising from the molecular interaction is
introduced. The adjustable binary interaction parameter in the P-V EOS is incorporated as a
correction for the binary interaction energy. In the S-L EOS, the binary interaction term
modifies the characteristic pressures. Thus, it has a different physical meaning.
With much similarity to the F-H or S-L EOS theories, the Simha-Somcynsky (SS)
model [68] originates from treating molecules as segments on a lattice. In the case of a
mixture, a lattice contains both species, which are divided into approximately equal-sized
segments. Nonetheless, unlike the other theories, the SS theory allows for a pressure- and
temperature-dependent fraction of vacancies or holes that express free-volume within the
lattice. This accounts for molecular disorder in the lattice model. The equations derived from
the SS theory incorporate the temperature- and pressure-independent parameters that account
for intra- and intermolecular interactions within the mixture's components.
Based on the lattice fluid model, Rodgers and Sanchez [71] determined that adding an
empirical correlation for the interaction parameter would improve the predictive scope of the
LF model. With the addition of this correlation using Hansen's three-dimensional solubility
parameters [72], the LF model was reported to be able to predict solubilities in all types of
gas/polymer systems without the use of adjustable parameters. In other words, only the pure
component equation-of-state and solubility parameters are required.
28
Curro et al. used the Polymer Reference Interaction Site (PRIS) theory [73, 74] to
compute the sorption of a monatomic gas in a polymer liquid. This theory describes the
intermolecular packing between polymer chains and solute using the integral equation theory
of molecular liquids. Also, the chemical potentials of the solute species in the polymer must be
obtained in order to calculate the sorption of a gas in a polymer liquid.
29
CHAPTER 3. RESEARCH METHODOLOGY FOR PVT AND
SOLUBILITY STUDY
3.1 Introduction
Gas solubility in polymers can be measured using different techniques, that is,
gravimetric techniques, including vibrating or oscillating techniques; PVT techniques with the
pressure decay method; and gas-flow techniques. A brief review of the technique which was
implemented is given below, followed by the description of a technique we recently developed
that couples a new gravimetric technique with a PVT visualization technique.
3.2 Theoretical Background
Theoretical models to determine the solubility and swelling of the polymer/gas mixture
such as the Sanchez and Lacombe (SL) [45-47] and the Simha and Somocynsky (SS) EOS
[68] are all based on the statistical thermodynamic theory.
The equation of state of the pure component system is written in the following manner for the
SL EOS:
3.1
or the SS EOS:
30
3.2
3.3
In the above relations, ~,~
,~
PT and V~
are reduced parameters. They are calculated from the
characteristic reducing parameters P*, T*, V* and as follows:
3.4
where y is the fraction of occupied lattice sites, s is the number of segments per chain of molar
mass, c is the number of external degrees of freedom per chain, and finally V~
and
are dimensionless quantities.
The solubility of gas in the polymer (binary system) can be calculated theoretically using the
phase equilibrium theory:
3.5
31
where is the chemical potential of gas in the gas phase and is the chemical potential of
gas in polymer/gas mixture phase. Under the phase equilibrium condition, the mass fraction of
gas in the polymer/gas mixture phase, i.e., the theoretical solubility , can be obtained
by solving Eq. (3.5).
In the case of SS-EOS, Eq. (3.6) was used to solve [75]:
3-6
And Eq. (3.7) was used to calculate [36, Gli paper]:
3-7
where is the molar free energy of the polymer/gas mixture [36 Gli paper].
3-8
In the case of SL-EOS, Eq. (3.9) and Eq. (3.10) were used to determine and :
3-9
32
3-10
The swollen volume can be obtained from the following relation:
3-11
where S is the gas solubility (g-gas/g-polymer) in the polymer melt which is calculated from
the EOS, m (g) is the initial weight of the polymer sample, vp,pure (cm3/g) is the specific volume
of pure polymer.
3.3 Methodology and Approach
The details of the measuring procedure using MSB can found in our previous literature
[76]. The amount of gas which is absorbed by the polymer can be determined by the following
equation:
3-12
where W(P,T) is the weight of the sample at temperature T and pressure P; W(0,T) is the
weight of the sample at temperature T and vacuum; ρgas is the density of the gas inside the
33
chamber at temperature T and pressure P; VB, VP, and VS are the volume of the sample holder,
the volume of pure polymer, and the swollen volume of polymer, respectively, due to gas
dissolution at temperature T and pressure P.
By ignoring the polymer’s swollen volume (VS) in Eq. 1, the measured weight gain Wg
in Eq. (3.12) can be transformed to the apparent solubility (Eq. 3.13), Xapparent, which is less
than the actual solubility:
3-13
As shown in Eqs. 3.12 and 3.13, it is impossible to measure the accurate solubility of
the gas in the polymer melt by ignoring the swollen volume (VS). However, presently, there is
a lack of reliable and accurate PVT data for polymer/gas mixtures which are measured
experimentally. Hence, the swollen volume is typically estimated by an equation of state
(EOS) which can be applied to a two-component mixture system under equilibrium.
A general approach that combines the experimental solubility measurement and the
thermodynamic models was proposed by Li et al. [77] Firstly, a gravimetric method is carried
out to experimentally measure the gas sorption in a polymer melt (apparent solubility, Xapparent).
Secondly, the SS-EOS or SL-EOS is applied to calculate the phase equilibrium (theoretical
solubility, Xtheory) and the swollen volume of polymer, Vs. Thirdly, the theoretically predicted
swollen volume, Vs can be used to complete the correction on the apparent solubility, Xapparent,
and then to obtain the actual solubility or corrected solubility, Xcorrected. Meanwhile, the PVT
34
apparatus is also used to determine the swollen volume [78]. The swollen volume of the
polymer/gas mixture may also be obtained from the following relation:
3-14
where is obtained from measuring the volume of the polymer/gas drop mixture,
where as is obtained from PVT equation. The corrected solubility, Xcorrected, with the
buoyancy effect compensation can be obtained using Eq. 3.14:
3-15
3.4 Summary
Based on the magnetic suspension balance, a robust general research approach was
established for the calculation of solubility, which has been described in detail in the previous
chapter. In order to obtain accurate solubility data, buoyancy effect must be accounted for,
which is generated due to the swelling behavior of the polymer in the presence of a gas.
Experimental and theoretical approaches have been implemented in order to account for the
swelling behavior of the polymer/gas mixture melt. The phase equilibrium and the PVT
behavior of the polymer/supercritical fluid are studied in detail with the theoretical approach
proposed by Dr. Guangming Li and the experimental approach put forward by Dr. Yao Gai
Gary Li.
The results showed that the SS-EOS predicted the swelling and hence the solubility of
carbon dioxide in PLA in close proximity of the theoretical values in comparison to SL-EOS.
35
CHAPTER 4. SOLUBILITY AND SWELLING BEHAVIOR OF
PLA IN PRESENCE OF CO₂
4.1 Introduction
Based on the magnetic suspension balance, a general approach was established to
measure the solubility of carbon dioxide. In order to obtain accurate solubility data, inclusion
of the swelling volume is essential, which is generated from the dissolution of the blowing
agent in the polymer.
The theoretical approach for the determination of swollen volume and phase
equilibrium was built on a variety of technically sound thermodynamic models, such as SS-
EOS and SL-EOS. Previous work [75] has illustrated some deviation among the
thermodynamic models in terms of theoretical solubility and swollen volume prediction. In
this chapter, a systematic investigation is illustrated to investigate the factors that govern gas
solubility in a polymer. The two models, namely SS-EOS and SL-EOS, are compared with the
experimental results in terms of their ability to predict theoretical solubility and volume
swelling.
Three different grades of PLA are utilized to investigate the effect of D-content on
solubility and swelling. The effect of varying molecular weight and D-content on the gas
solubility and swelling volume is also investigated.
36
4.2 Experimental
4.2.1 Materials
Three different grades of Polylactide (PLA) from were used in the
experiments: PLA 3001D (1.4% D-content), ; PLA 8051D (4.6% D-
content), ; and PLA 4060D (12% D-content), . The
PLA was received in the form of pellets from LLC. Carbon dioxide
(Coleman grade, 99.99% purity) was obtained from BOC Canada.
4.2.2 PVT Data for PLA
The PVT data published by Sato for PLA was used to obtain the Tait’s equation [79].
The same Tait’s equation was used for the three different grades of PLA. Since A Tait’s
equation represents the PVT behavior of a polymer, therefore, generalizing a Tait’s equation
for different grades of PLA is not preferable. This makes it harder to observe the effect that
different variables have on the solubility, swelling volume, and surface tension. The latter
notion is discussed in depth later in the Chapter.
4-1
In the above equation, the temperature, T, is in (°C) and pressure, P, is in (bars). The PVT data
obtained was also used to derive the characteristic parameters for both SS-EOS and SL-EOS:
P*, V*, T*. All the characteristic parameters for the PLA grades are listed in Appendix 3.
37
4.3 Solubility of CO₂ in PLA (Binary System)
4.3.1 Swelling Behavior of PLA in Presence of CO2
4.3.1.1 Experimental Setup
The experimental setup consisted of the following components: a high-pressure
chamber with a sapphire window for the purpose of visualization; a 2024 x 2024 resolution
JAI Pulnix TM4100 CL camera with control software; Schneider 4/80 lens and extension
tubes; a temperature controller (Omega CN132) with thermocouple (Omega RTD); two
cartridge heaters; an automatic high-precision XY stage with Galil motion controller and
control board; a manual 1 in. XYZ stage to adjust the position of the light source; a syringe
pump connected to the gas tank; and a backlight source with a light equalizer/diffuser.
4.3.1.2 Experimentation
PLA samples were sliced from a strip obtained from a micro compounder and weighed
using a precision microbalance. The selected PLA samples were attached to the droplet rod to
form the sessile drop for each experiment. Swelling measurements for mixtures
were conducted at two different temperatures, 453 K and 473 K. At each temperature, the
pressure of CO2 inside the chamber was varied from 6.894 MPa (1000 psi) to 20.684 MPa
(3000 psi) in 3.447 MPa (500 psi) increments. Each pressure level was maintained for 1.5
hours to ensure that the equilibrium conditions were established for the polymer/gas solution.
Equilibrium was considered to be achieved when the total volume of the polymer/gas solution
no longer changed.
38
In order to compare the experimental data with the theoretical, SS-EOS and SL-EOS
were used to determine the theoretical volume swelling ratio. The parameters used to
determine the theoretical swelling ratio ( ) are shown in Appendix 3.
4.3.1.3 Pressure and Temperature Effect on Volume Swelling
It was observed that the volume of the PLA3001D/CO2 mixture increased with an
increase in pressure as illustrated in Fig. 4.1 and Fig. 4.2. Due to the increase in pressure inside
the chamber, the density of the CO2 gas increases, hence more CO2 molecular will penetrate
into the PLA polymer matrix causing more dilation until it reaches the saturation point.
With a fixed temperature, an increase in pressure causes an increase in the volume of
the polymer/gas mixture, as well as the volume swelling ratio. Since the solubility of CO2
increases [80] as the pressure is increased, more CO2 gas is permitted to enter the PLA melt
matrix, hence an increase in swelling volume was observed. The hydraulic pressure effect due
to the CO2 was accounted for by using Tait’s equation. The Tait’s equation obtained from the
PVT apparatus was compared with the Tait’s equation obtained through parameters based on
the PVT data of PLA by Sato et al. for SS-EOS and SL-EOS [79].
At isobaric conditions, the volume swelling of the PLA/CO2 mixture tends to decrease
as illustrated in Figures 4.1-4.3 with an increase in the temperature. As the temperature
increased, the polymer chains became softer which increased the free volume as well as
specific volume. The solubility of CO2 in PLA is known to decrease as the temperature
increases [81]. This means that the diffusion of CO2 out of the polymer increased; hence more
CO2 is forced out of the polymer/gas mixture compared to what would enter due to the free
volume at an elevated temperature. In other words, despite the increase in the free volume
39
within the PLA/ CO2 matrix, CO2 will escape out of the matrix. For instance, at the 13.79 MPa
pressure level and 453 K; PLA-3001D/CO2 has a volume swelling ratio of 9.32%; whereas at
473 K, the swelling ratio is 8.88%.
180 185 190 195 200
1.04
1.06
1.08
1.10
1.12
1.14S
we
llin
g R
atio
(%
)
Temperature (Celcius)
1000 psi
1500 psi
2000 psi
2500 psi
3000 psi
PLA 3001D
Figure 4-1: Effect of Temperature variance on Swelling Ratio for PLA3001D
180 185 190 195 2001.02
1.04
1.06
1.08
1.10
1.12
1.14
Sw
elli
ng
Ra
tio
(%
)
Temperature (Celcius)
1000 psi
1500 psi
2000 psi
2500 psi
3000 psi
PLA 8051D
Figure 4-2: Effect of Temperature variance on Swelling Ratio for PLA8051D
40
180 185 190 195 2001.02
1.04
1.06
1.08
1.10
1.12
1.14
Sw
elli
ng
Ra
tio
(%
)
Temperature (Celcius)
1000 psi
1500 psi
2000 psi
2500 psi
3000 psi
PLA 4060D
Figure 4-3: Effect of Temperature variance on Swelling Ratio for PLA4060D
4.3.1.4 Comparison of the Experimentally Measured Data and
Theoretically Predicted Data
The experimental data obtained using the in-house PVT apparatus [82] was compared
with the swelling volume ratio obtained via EOS. SS-EOS and SL-EOS were implemented in
order to calculate the theoretical swelling volume ratio [83]. It was evident from Figure 4.4-4.9
that the SS-EOS provides a more realistic prediction of the swelling volume ratio; whereas the
SL-EOS exaggerated the swelling volume ratio with respect to the experimental result. This
has been illustrated in our previous work in detail [82, 84, 85].
41
1000 1500 2000 2500 3000
1.04
1.06
1.08
1.10
1.12
1.14
1.16
1.18
1.20
1.22
Sw
ell
ing
Ra
tio
Pressure (psi)
3001D EXP
3001D SS-EOS
3001D SL-EOS
180 oC
Figure 4-4: Swelling Ratio of PLA3001D at 180 °C with varying pressure
1000 1500 2000 2500 30001.02
1.04
1.06
1.08
1.10
1.12
1.14
1.16
1.18
1.20
1.22
Sw
ell
ing
Ra
tio
Pressure (psi)
8051D EXP
8051D SS-EOS
8051D SL-EOS
180 oC
Figure 4-5: Swelling Ratio of PLA8051D at 180 °C with varying pressure
42
1000 1500 2000 2500 30001.02
1.04
1.06
1.08
1.10
1.12
1.14
1.16
1.18
1.20
1.22
Sw
ell
ing
Ra
tio
Pressure (psi)
4060D EXP
4060D SS-EOS
4060D SL-EOS
180 oC
Figure 4-6: Swelling Ratio of PLA4060D at 180 °C with varying pressure
1000 1500 2000 2500 30001.00
1.02
1.04
1.06
1.08
1.10
1.12
1.14
1.16
1.18
1.20
Sw
ell
ing
Ra
tio
Pressure (psi)
3001D EXP
3001D SS-EOS
3001D SL-EOS
200 oC
Figure 4-7: Swelling Ratio of PLA3001D at 200 °C with varying pressure
43
1000 1500 2000 2500 30001.00
1.02
1.04
1.06
1.08
1.10
1.12
1.14
1.16
1.18
1.20
Sw
ell
ing
Ra
tio
Pressure (psi)
8051D EXP
8051D SS-EOS
8051D SL-EOS
200 oC
Figure 4-8: Swelling Ratio of PLA8051D at 200 °C with varying pressure
1000 1500 2000 2500 30001.00
1.02
1.04
1.06
1.08
1.10
1.12
1.14
1.16
1.18
Sw
ell
ing
Ra
tio
Pressure (psi)
4060D EXP
4060D SS-EOS
4060D SL-EOS
200 oC
Figure 4-9: Swelling Ratio of PLA4060D at 180 °C with varying pressure
44
4.3.1.5 Effect of ‘D’ Content/Molecular Weight on Volume Swelling
It was observed that at 453 K, PLA3001D has a higher volume swelling ratio than PLA
8051D. For example, at 17.24 MPa, PLA 8051D (D content of 4.6%) has a volume swelling of
11.29%; whereas PLA 3001D (D content of 1.4%) has a volume swelling of 12.21%. Similarly,
the swelling ratio of PLA 4060D at 17.24 MPa is 10.81%, which was less than that of PLA
8051D. At this instant, we cannot conclusively state the D-content’s effect on the volume
swelling. This is due to the presence of two variables, the D-content and molecular weight. In
order for us to state any concrete effect of the D-content, we need to experiment with two PLA
samples with similar, if not the same, molecular weight and different D-content.
1000 1500 2000 2500 30001.02
1.04
1.06
1.08
1.10
1.12
1.14
1.16
Sw
ell
ing
Ra
tio
(%
)
Pressure (psi)
3001D EXP
8051D EXP
4060D EXP
180 oC
Figure 4-10: Effect of varying D-content/Mw on swelling ratio at 180 °C
45
1000 1500 2000 2500 3000
1.02
1.04
1.06
1.08
1.10
1.12
1.14
1.16
Sw
ell
ing
Ra
tio
(%
)
Pressure (psi)
3001D EXP
8051D EXP
4060D EXP
200 oC
Figure 4-11: Effect of varying D-content/Mw on swelling ratio at 200 °C
4.3.2 Solubility of CO2 in PLA
With the prediction of swollen volume from SS-EOS and SL-EOS and the
experimental data (mentioned in Sec. 4.3.1), the solubility of in PLA at 180 °C and 200
°C was obtained by utilizing the apparent solubility obtained from the MSB. Methodology
using the MSB has been discussed at length in Chapter 3.
4.3.2.1 Pressure and Temperature effect on Solubility of CO₂ in PLA.
The effect of