Simulating the Misting of Lubricant in the Piston Assembly of an Automotive Gasoline Engine: The Effect of Viscosity Modifiers and Other Key Lubricant Components

The apparatus developed for this study utilised a venturi mist generator to produce an oil mist flow. This flow was measured using a particle sizer, and by weighing the oil in various flows before and after the test, Fig. 2.

Oil was fed into the throat of the venturi mist generator using a motorised syringe pump. The venturi reproduced conditions at the peak flow through the top ring a of a gasoline engine at 2500 rpm, 75% load and 50% throttle, as reported and derived from the model of Gamble et al. [28], Table 1. Dimensions are shown in Fig. 3. The lubricant inlet was raised approximately 1 mm above the venturi throat surface, so that the lubricant flowed over a distinct edge, as in the piston ring gap. This feature was accounted for in the flow calculations. The expansion ratio of the venturi is the ratio of the outlet duct area to the throat area. The venturi was supplied with air from a laboratory compressed air supply via a coalescing filter with a 0.01 μm element and a pressure regulator. At an inlet air pressure of 0.15 MPa, the venturi was choked and the flow parameters are as listed in Table 1. Conditions correspond well to those in the engine in all but pressure and temperature. The effect of pressure was considered secondary as this mist formation mechanism is controlled by shear between the gas and lubricant flow, where similarity in velocity and flow rate is of greater importance. The lower temperature in the lab test may have influenced droplet formation and droplet size distribution, as viscometric, viscoelastic and extensional properties vary with temperature [41, 42]. Further work to measure droplet distributions extracted from the crankcase of a fired engine was performed: The effects of temperature on droplet formation will be best clarified in future publications by comparing between the lab and engine environments.

The mist flow was directed, via an 8 mm pipe, through a laser diffraction particle sizer, that measured droplets with diameters between 0.1 and 1000 µm that passed through the 10 mm diameter beam. Data were collected continuously, recorded every second and averaged for the duration of the test. The distribution was presented as the proportion of the Total Flow Volume at each droplet diameter, the Volume Frequency: This was most relevant to bulk flow mechanisms, rather than number of droplets or proportion of the total surface area. Figure 4 shows a typical droplet size distribution. In this and almost all cases observed the distributions were tri-modal, i.e. three characteristic droplet diameter ranges. The largest had diameters of 135–1000 μm, typical of what is termed spray, where droplet inertia is high and they quickly deposit from the flow. These were not thought to form readily in the piston assembly, as they are of similar size to the ring gap. Droplets with diameters of 18–135 μm were present in almost every test. These droplets were typical of mist flows, where inertia is overcome by aerodynamic forces and droplets stay entrained in the gas flow, but are rapidly deposited from a flow as its velocity reduces. The smallest droplets, with diameters of 0.1–18 μm were typical of aerosol flows, where inertia is extremely low, entrainment in the gas flow is dominated by Brownian motion and, therefore, aerosol droplets are present even in stationary flows. Aerosol flows weren’t present in many tests. The mist and aerosol droplets were thought to be representative of those found in the engine [43]. Aerosol and mist ranges were termed the minor and major misting region, respectively, in this study. Characteristic Droplet Diameters were defined by the droplet diameter at the peak of each distribution bell curve.

The tendency to form droplets was measured by weighing the bulk liquid lubricant flowing into and out of the system. The lubricant entering the mist generator was calculated by weighing the syringe and feed line before and after each test and subtracting to find the difference. The oil that dripped from the outlet pipe was collected in a beaker and, again, weighed before and after the test. As this oil was not entrained in the gas flow, it was assumed to contain lubricant that has not formed droplets and/or droplets deposited on the pipe walls, i.e. this was unmisted oil. As it was not possible to collect all the droplets entrained in the gas flow, the weight of oil leaving the system as droplets was calculated by subtracting the unmisted oil from the total input:where M_droplets is the total oil leaving the system as droplets, M_in is the total oil entering the system and M_{unmisted out} is the total oil leaving the system unmisted. The tendency of a lubricant to form droplets was defined as total quantity of oil leaving the mist generator as droplets as a percentage of the total entering the system:

In order that the measurements of the output values were more accurate, the outlet pipe from the mist generator was lined with PTFE so that oil would not wet the surface and be retained in the system, but would flow out under shear from the gas flow.

The syringe charged with oil, the oil feed tube and the unmisted oil collection beaker, Fig. 2, were weighed. The syringe was compressed until the oil feed tube was full of oil. The particle sizer self-calibrated and data recording commenced. The air supply was switched on, set to 0.15 MPa and left for 10 s to allow the flow through the system to become steady. The syringe pump started and the inlet feed attached. The test duration was two minutes, starting when the oil entered the venturi (indicated by an audible change in gas flow). The test was ended by stopping the particle sizer and the syringe pump, clamping and disconnecting the oil feed pipe to prevent further oil flow. The air supply was kept running for a further 5 min to ensure that all oil was removed from the system. The mass change of the syringe, the oil feed tube, unmisted oil collection beaker, and the drip tray before and after the test provided M_in and M_{unmisted out}, and by subtraction M_droplets. Data from the particle sizer were recorded and averaged for the two-minute test period.

As the flow rate of air in the venturi was fixed, the misting process was controlled by the flow rate of oil. Figure 5 shows the misting tendency of an API Group III SAE 5W base oil and an API Group III 5W30 fully formulated lubricant at a range of oil inlet flow rates and the droplet size distributions at selected positions on the curve. As the inlet flow rate increased, the misting tendency initially decreased and then increased greatly above approximately 5 ml/min until almost all the oil formed droplets. At lower flow rates, the majority of droplets were in the major and minor misting regions. Above 9 ml/min, the droplets were almost entirely spray-sized droplets. It was hypothesised that a greater oil flow rate caused a greater accumulation of oil at the oil feed. Above a certain oil flow rate, approximately 9 ml/min in these cases, the droplet formation mechanism changed from ‘rolling’ to ‘undercutting’, as described by Hewitt et al. [44] and Fig. 6. The rolling mechanism was thought to be representative of the droplet formation at piston ring gaps and component edges. The undercutting mechanism was thought to be more representative of blow-through, e.g. at the cylinder-liner interface or in the oil control ring. Repeatability was low at low flow rates, below approximately 2.5 ml/min.

As both rolling and undercutting were representative of droplet formation mechanisms in the engine, the range of oil flow rates used in these tests was generally 3-9 ml/min, allowing observation of both mechanisms and the transition between them. For a small number of lubricants, the transition from rolling to undercutting occurred outside of this range. Where feasible, the range was extended to accommodate this.

The undercutting mechanism was evaluated by considering several key parameters at a condition in the region of approximately linear increase in droplet formation tendency with oil inlet flow rate (i.e. significantly away from the transition so that the gradient of the curve was close to linear). An oil inlet flow of 9 ml/min met this condition for almost all lubricants. These parameters were %droplets, the gradient of the curve at this point and the linearly projected abscissa intercept of the curve from this point, Fig. 7.

The region of linear increase in droplet formation tendency was thought to be a superposition of the rolling droplet formation, which had low %droplets, and the undercutting droplet formation, which had higher %droplets. As the oil inlet flow rate increased, the quantity of lubricant at the throat of the venturi subject to the undercutting mechanism increased and the overall %droplets increased. Counterintuitively, a greater resistance to droplet formation by the undercutting mechanism produced a higher %droplets value, i.e. the resistance to droplet formation caused a greater quantity of the lubricant being exposed to the undercutting mechanism and a steeper curve. The complexity of droplet formation is exemplified by this greater ‘resistance to shear and pressure-driven droplet formation’ causing more droplets to be produced, as lubricant accumulates and blows through rather than flowing.

Several repeated tests were conducted using different lubricants at various conditions. Parameters used to define the statistical significance of results and interpretations are in Table 2.

Figure 8 shows the misting tendency of PAOs of varying molecular weight and viscosity at a range of oil flow rates. At low flow rates, base oils with lower molecular weight and viscosity produced droplets more readily. As molecular weight and viscosity decreased, transition from a rolling to an undercutting mechanism occurred at a higher flow rate. This can be attributed to the lower resistance to shear exhibited by lower viscosity oils: Oil was more quickly removed from the venturi under shear and did not accumulate as much as a higher viscosity oil under the same conditions.

Figure 9 shows the variation in misting tendency of oil with average molecular weight. These were tests with an inlet oil flow rate of 3 ml/min, where the greatest proportion of mist-sized droplets was formed. Misting tendency varied inversely and linearly with molecular weight.

Figure 10 shows that the dynamic viscosity at 20 °C for these oils varied with molecular weight to the power of 3.35. Thus, misting tendency variation with dynamic viscosity at 20 °C can be described using a third order polynomial, Fig. 11, as could be expected from a combination of Fig. 9 and Fig. 10: Greatly increasing misting tendency with a decrease in dynamic viscosity.

Figure 12a–d shows the droplet size distributions for the tests described in Fig. 9 and Fig. 11. As the proportion is volumetric, the apparently substantial proportion of spray in these distributions was contained in relatively few droplets. There was a large quantity of mist-sized droplets in each distribution, especially in the major mist region. PAO 2 and PAO 6 had comparable characteristic diameters, approximately 34 μm. PAO 8 had a larger characteristic diameter, approximately 63 μm, consistent with previous findings that higher viscosity oils produce larger droplets [45, 46]. The distribution for PAO 4 was different but the reason for this was not clear.

Figure 13 shows the variation in misting tendency of oils with similar viscosity but of different API Groups, again at an oil inlet flow rate of 3 ml/min. Fully formulated reference oil was included for comparison. There was no significant difference in the misting tendencies between the refined oils (I-III). Group IV oil, PAO, showed significantly greater misting tendency. This may arise from differences in molecular structure between refined hydrocarbons (slightly branched linear chains) and PAO, which is mainly trimer and tetramer of decane with a star-type structure.

Figure 14 shows the misting tendency of Group III SAE 5W lubricants containing single commercial additives at an oil inlet flow rate of 3 ml/min. The commercial fully formulated lubricant, FF, and the base oil reference, Gp III, were included. Fully formulated lubricant had a much lower tendency to form droplets than its base oil under the same conditions. The blend containing viscosity modifier, VM, behaved comparably to the fully formulated lubricant, indicating that VM has a dominant role in reducing misting tendency. Detergent 2, Det 2, and silicone antifoam, AF, significantly increased misting tendency. Detergent 1, Det 1, or dispersant, Disp, did not significantly affect the misting tendency of the base oil. Some additives altered the viscosity, Table 3, but viscosity didn’t correlate significantly with misting tendency in Fig. 14.

Figure 15 shows the droplet size distributions for the tests in Fig. 14. Distributions for the fully formulated lubricant and the viscosity modifier blend were narrow with no clear pattern. The relatively small quantities of droplets, due to the influence of the viscosity modifier, caused these tests to have less statistical repeatability than for lubricants with higher misting tendency. Droplets in the major mist region for the reference base oil, the blends containing viscosity modifiers or detergent have similar characteristic diameter, approximately 46 μm. The distribution for oil containing antifoam was tetramodal with two characteristic diameters in the major mist region. The distribution for oil containing dispersant had characteristic sizes outside the established regions. Significant quantities of minor mist-sized droplets were observed when surface-active additives were present, i.e. detergents, dispersant and antifoam. These additives probably affected the liquid/air interfacial properties: This could be investigated using, e.g. the Weber Number [47], the ratio between inertia and surface tension forces, but was beyond the scope of this study.

Including a polymeric viscosity modifier had the greatest effect on reducing the misting tendency of lubricants. The viscoelastic properties of such polymer-containing fluids alter the extensional behaviour. As discussed by Dasch et al. [38], Marano et al. [45] and Smolinski et al. [46], higher extensional viscosity induced by the presence of polymers reduces the tendency of a fluid to break into droplets under shear and extension. These effects were more significant than changes in surface properties induced by the presence of surface-active additives; detergents, dispersant and antifoam. This broadly correlated with the observations of Ohmori et al. [48], where polymer additives significantly increased extensional breakup time, but that surfactant additives had little effect.

Table 5 shows polymer and blends properties. Only a few blends had were semi-dilute (i.e. entanglement density > 0.1), generally high concentration linear polymer blends. Star polymers had entanglement densities around an order of magnitude lower than linear polymers, i.e. no significant intermolecular interaction. At engine temperatures, larger hydrodynamic volumes could cause semi-dilute interactions in more blends.

Polymers 1 and 2, high molecular weight linear OCPs, had similar hydrodynamic volumes, but Polymer 1 had higher self-concentration, indicating tighter coiling. Polymer 3, a low molecular weight OCP, had extremely small hydrodynamic volume and extremely high self-concentration relative to other OCPs. This indicated either extreme high coiling or that molecules were sufficiently short to not coil significantly. The latter was more likely, suggesting low potential for further extension of Polymer 3 molecules.

Polymer 4, a high molecular weight styrene-butadiene, produced the lowest entanglement densities of the linear polymers. The thickening effect was high, so concentrations were relatively low. The large hydrodynamic volume and low self-concentration indicated low coiling. The larger styrene side groups appeared to hinder coiling. Thus, the potential for extension of this molecule was lower than an OCP of similar chain length [55].

Polymers 5 to 7, star polymers, showed different behaviour. Hydrodynamic volumes were higher than the linear polymers. Due to the dense molecule core and the coiling of the arms, self-concentration was extremely high. However, as the arms are fixed in the core, or physically attracted (Polymer 6), bending and extension was hindered, hence the stronger correlation with arm molecular weight than total molecular weight [50].

Figure 18 and Table 6 show misting tendency and droplet distribution characteristics for polymer blends at low inlet flow rate, 3 ml/min, ‘rolling’ or misting conditions. Table 7 and Table 8 show droplet formation parameters and droplet distribution characteristics for polymer blends at higher inlet flow rate, 9 ml/min, i.e. ‘undercutting’ or blow-through conditions.

Figure 19 shows droplet formation tendency and droplet size distribution at 3 ml min⁻¹ for Polymer 1, a high molecular weight OCP. Droplet formation tendency was dramatically reduced under all conditions. Behaviour was independent of polymer concentration and viscosity. There was a relatively high proportion of mist-sized droplets, 27.8–60.7%, Table 6, and an increase in the characteristic droplet diameters in blends using higher viscosity base oil, 73 μm versus 40-54 μm.

Figure 20 shows results for Polymer 2, a high molecular weight OCP. Droplet formation tendency was reduced by 1.5–2.3% at 3 ml min⁻¹, Fig. 18. The proportion of mist and aerosol (6.0–12.5%) was greatly reduced versus 8cSt base oil (60.7%), Table 6. Transition to undercutting occurred at lower flow rate, Table 7. At high flow rates, droplet formation tendency increased with polymer concentration. Characteristic spray droplet diameters were greater under all conditions (540 μm) than 8cSt base oil (460 μm). Mist was suppressed in the 8cSt blend and aerosol was suppressed in the 12cSt blend from 8cSt base oil. Characteristic mist droplet diameter was greater at the highest polymer concentration, 63 μm versus 40 μm, Table 8.

Figure 21 shows results for Polymer 3, a low molecular weight OCP. Droplet formation tendency correlated with blend viscosity: The 8cSt blend and 8cSt base oil were insignificantly different, as also for 12cSt blends. There was relatively high proportion of mist and aerosol (39.7% for 8cSt blend versus 60.7% for 8cSt base oil) and the consistent presence of aerosol-sized droplets with diameters of ~ 0.5 μm, Table 6, Fig. 21. Some blends were semi-dilute but entanglement effects were not significant. Base oil dependency was seen, Table 7: Abscissa intercepts for 8cSt and 12cSt blends from 4cSt base oil were insignificantly different, but was greater for the 12cSt blend from 8cSt base oil.

Figure 22 shows results for Polymer 4, a high molecular weight styrene-butadiene. Polymer-dominated behaviour was indicated by differences in droplet formation between 8cSt blend and 8cSt base oil. However, viscosity dependence was greater, indicated by similar droplet formation tendency for 12cSt blends despite different polymer concentration, Tables 6 and 8. There was some aerosol formation.

Figure 23 shows results for Polymer 5, a high molecular weight styrene–isoprene star. 12cSt blends produced similar sized droplets, larger than the 8cSt blend (460–540 μm vs. 116 μm), Table 6. The 8cSt blend produced a significant quantity of aerosol (4.9%). Misting tendency correlated with viscosity, also characteristic droplet diameters for spray. There was insignificant difference in misting tendency between the 12cSt blends, and between the 8cSt base oil and 8cSt blend, Fig. 18

Figure 24 shows results for Polymer 6, a micellar-type styrene–isoprene star polymer. The star structure of this polymer dissociates under shear into individual arms of short chain linear polymers (molecular weight ~ 6500 Da, around 30% greater than Polymer 3, i.e. low). Misting tendency of the 8cSt blend was insignificantly different to 8cSt base oil, Fig. 18, and there was significant formation of aerosol (0.1–1.8%), Table 6. Because blend viscosity was calibrated to the star structure, dissociation will have changed the high shear viscosity: Droplet formation curves had similar profiles but varying abscissa intercepts, Table 7.

Figure 25 shows results for Polymer 7, a high molecular weight fixed isoprene star. Viscosity dependence was greater than viscoelastic effects. The 12cSt blends behaved comparably overall, producing higher proportions of spray than the 8cSt blend (78.6–89.4% vs. 51.2%), Tables 6 and 8. The 8cSt polymer blend generated lower aerosol proportion (9.0% vs. 35.0%) than 8cSt base oil, Table 6.

At low flow rate, misting conditions, the higher molecular weight star (Polymer 5) produced larger mist and aerosol droplets in 8cSt blends, Fig. 18. In 12cSt blends, the high molecular weight star suppressed mist and aerosol formation substantially: The lower molecular weight star reduced mist and aerosol proportion substantially versus 8cSt base oil.

Behaviour at high flow rates, spray conditions, was similar for both polymers except that, in Polymer 7, the 12cSt blend from an 4cSt base oil had lower misting tendency than the 12cSt blend from an 8cSt base oil—Inverse to Polymer 5, Table 7. Although the smaller molecules of Polymer 7 store less energy individually than Polymer 5 (lower self-concentration and arm molecular weight), higher concentration was required to achieve the blend viscosity, so perhaps the total quantity of potential extensional energy per unit finished blend was higher. This suggests that potential viscoelastic energy could be controlled somewhat independently of thickening effect.

At low flow rates, 3 ml/min, misting conditions, the micellar star polymer (Polymer 6) produced less mist and aerosol in 8cSt blends than fixed star Polymers 5 and 7 (1.8% vs. 48.8% and 64.9%), Table 6. Dissociation means micellar star arms are, functionally, linear polymers, so energy dissipation may be greater than fixed star arms, which are constrained at one end and hindered.

At high flow rate, 9 ml/min, spraying conditions, the micellar star polymer produced more mist and aerosol-sized droplets than fixed stars (7.4% vs. 1.3% and 2.8%), Table 8. Projected abscissa intercepts for micellar stars varied due to micelle dissociation affecting viscosity, Table 7. Overall, differences in misting tendency under spray conditions correlated more strongly with viscosity. For all star polymers, fewer aerosol-sized droplets were formed in higher viscosity base oil (12cSt blend from 8cSt base oil).

Polymer 1 greatly suppressed droplet formation but Polymer 2 did not generate such dramatic reduction. Polymer 1 was more tightly coiled and had greater capacity for energy dissipation in extension. At low flow rate, 3 ml/min, misting conditions, the 8cSt blend of Polymer 1 produced larger droplets in mist, spray and aerosol regions versus 8cSt base oil. However, Polymer 2 did not produce mist-sized droplets. 12cSt blends from 8cSt base oil both produced little or no aerosol compared to 12cSt blends from 4cSt base oil, Table 6.

At high flow rate, 9 ml/min, spray conditions, dramatic differences in misting tendency were observed. Polymer 1 blends had misting tendencies factors of 3 to 11 lower than equivalent Polymer 2 blends, Table 7. None of these blends were semi-dilute (no significant intermolecular interaction), suggesting viscoelasticity differences as a root cause.

Merely including Polymer 1 appeared to define behaviour. Polymer 2 showed some base oil and concentration dependency: At 3 ml/min the 12cSt blend from 4cSt base oil produced larger mist droplets (63 μm vs. 40 μm) but greater proportion of aerosol (5.8% vs. 0%) versus 12cSt blend from 8cSt base oil.

Droplet formation tendency of the 8cSt Polymer 3 blend, short-chain OCP, was not significantly different to 8cSt base oil—But was significantly lower using Polymer 2, a long chain OCP. A low concentration of long-chain molecules more effectively reduced droplet formation than a high concentration of short-chain molecules. Polymer 3 reduced aerosol formation and generally increased characteristic diameters of droplets formed, when compared to 8cSt base oil. Higher potential energy storage under extension in Polymer 2 effectively reduced mist and aerosol-sized droplet formation, and, thus, overall misting tendency.

It was possible to get similar viscometrics but substantially different misting tendency, caused by viscoelastic differences. This was particularly clear at high flow rates, spray conditions, where Polymer 3 blends had significantly lower droplet formation tendency and greater projected abscissa intercept than the equivalent Polymer 2 blend, i.e. lower resistance to shear and extension. Because short chain molecules were easily repated (dissociated) and aligned with the shear axis, resistance to shear and extension was lower. Polymer 3 blends produced higher aerosol and mist proportion than equivalent Polymer 2 blends (1.6–5.2% vs. 1.2–2.2%), Table 8. The lower droplet formation influence of Polymer 3 produced greater difference in mist and aerosol formation between the two 12cSt blends using different base oils. Lower mist proportion was formed in 8cSt base oil blends. Little difference in characteristic droplet diameters and proportions between the two 12cSt blends was observed in Polymer 2 blends, indicating greater dependence on polymer properties.

Polymer 2, a high molecular weight OCP, and Polymer 4, a high molecular weight styrene-butadiene are linear polymers. However, larger side groups and differences in base oil interaction meant styrene butadiene molecules did not coil as highly under low shear, indicated by lower self-concentration. Because Polymer 4 had greater chain length and hydrodynamic volume, a lower concentration was required to achieve blend viscosity than Polymer 2. Therefore, Polymer 2 blends had greater total capacity for energy dissipation in extension, shear and repation, because each molecule had greater extension capacity and there were more molecules in the blend.

At low flow rate, 3 ml/min, misting conditions, both polymers reduced mist-sized droplet formation in 8cSt blends. Polymer 4 blends generated high aerosol proportions in the 8cSt blend (16.3%) and 12cSt blends (7.3–9.4%), implying lower influence on energy dissipation in shear and extension, Table 6. Thus, energy dissipation in extension depended less on chain length (Polymer 4 = 4605, Polymer 2 = 2161) and more on capacity for extension, indicated by coiling and self-concentration.

At high flow rate, 9 ml/min, spray conditions, little difference in droplet formation tendency was observed, though curves gradients were higher for Polymer 2 blends than equivalent Polymer 4 blends, Table 7. This indicates that the OCP had a greater resistance to shear and extension, i.e. greater viscoelasticity and potential energy storage. Abscissa intercepts of Polymer 4 blends decreased with increasing polymer concentration but Polymer 2 blends had the same abscissa intercept, i.e. the viscoelastic contribution of Polymer 2 was more influential than concentration. 8cSt blends of Polymers 2 and 4 were the only such blends to produce significantly higher %droplets than 8cSt base oil under these conditions. This droplet formation mechanism seemed to have high viscosity-dependency, but these polymers increased resistance to shear and blow-through significantly. Similarly, 12cSt blends of Polymers 2 and 4 from 4cSt base oil had significantly higher gradient than all others, indicating increased resistance to shear due to viscoelasticity and, therefore, increased quantity of lubricant exposed to blow-through as flow rate increases.

Due to micellar dissociation under shear, both polymers acted, effectively, as short chain linear polymers. Arms of Polymer 6, micellar star polymer, had a chain length of 227, greater than Polymer 3 (175), a linear OCP. Dissociated, Polymer 6 arms had greater potential energy storage in extension or shear, and greater base oil solubility. Differences in treat rate to produce 8cSt blends were striking: Polymer 6 = 1.46%, Polymer 3 = 6.2%.

At low flow rate, 3 ml/min, misting conditions, both polymers effectively reduced aerosol formation compared to 8cSt base oil, Table 6. The micellar star polymer produced much lower mist-sized proportion than the OCP under the same conditions. In 12cSt blends from 8cSt base oil, Polymer 6 suppressed both mist and aerosol formation but the equivalent Polymer 3 blend produced 24.9% mist-sized droplets. Both polymers produced higher mist-sized proportion in 12cSt blend from 4cSt base oil, despite higher polymer concentrations.

At high flow rate, 9 ml/min, blow-through conditions, droplet formation behaviour correlated greatest with viscosity: There were insignificant differences between the droplet formation tendency of 8cSt blends and 8cSt base oil (18.9% vs. 19.2% and 20.2% for Polymer 3 and 6, respectively), Table 7. All OCP blends produced a significant quantity of aerosol droplets: The micellar star polymer suppressed aerosol formation in the 12cSt blend from 8cSt base oil, Table 8. Overall, the micellar star polymer behaved more like a short chain OCP than a fixed star, confirming micellar dissociation under shear. The minor differences in droplet size distributions and droplet formation tendencies seemed to occur where micellar star blend curves were offset, where micelle dissociation caused variation in real viscosity.

Unlike all other 8cSt polymer blends, Polymers 3 and 6 abscissa intercepts were insignificantly different to 8cSt base oil, i.e. lower influence on resistance to droplet formation.

In 12cSt polymer blends from 8cSt base oil, no significant difference in droplet formation tendency was observed for any of the polymers. This suggested that the higher viscosity base oil had a greater effect on behaviour than when a lower viscosity base oil or higher polymer content was used. In many blends, the polymer content of the 12cSt blends in 8cSt base oil was of similar magnitude to 8cSt blends from 4cSt base oil: The droplet formation of lubricants with lower viscosity base oils were more sensitive to the polymers they contained. This is logical, as lower viscosity base oils have a higher droplet formation tendency, Fig. 8.