There will be occasions when standards and guidelines stymie the development of new methods. For example, the majority of simulator studies utilized the international guideline specifying that cups will be positioned “Anatomically” (ISO-14242), i.e. acetabular liner is positioned above oscillating femoral head (Fig. 1). This can be disadvantageous for studies of “edge wear” in steeply inclined cups (Williams 2008, Leslie 2009, Angadji 2009). Importantly, such an “Anatomical” cup is fixed with respect to the resultant load-axis (Fig. 1d: R). This produces a constant edge-wear throughout the simulator's cycle. Our supposition was that it is more likely patients experience edge-wear intermittently, i.e. at extremes of motion. This intermittent effect can be best replicated with the cup mounted “Inverted” (Fig. 2), the rotating cam allowing precise selection of edge-wear at extreme of motion (Fig. 2c). An advantage of this method is that the wear-pattern in the orbiting cup is now much larger (Bowsher, 2009: x3.8 ratio), making edge-wear easier to achieve. Our hypotheses were that (1) the Inverted test would provide both “normal” and “edge wear” as defined (Clarke, 2015: steep-cup algorithm), (2) MOM wear rates under edge-wear condition would be greater than in standard simulator tests (Bowsher 2016) and (2) intermittent edge-wear of MOM cups (Inverted) would be less severe than in prior Anatomical tests (Williams 2008, Leslie 2009, Angadji 2009).

The 60mm MOM bearings (DJO, Austin TX) were selected on the basis of prior Anatomical study (Bowsher, 2009), were run with cups Inverted, using identical test methods as before, in the orbital simulator. Wear-rates in 60mm heads revealed both run-in and steady-state wear phases (Fig. 3a). The weight-loss method showed perturbations due to protein contaminants but these appeared of minor concern over 10-million cycles. One cup was damaged during set-up, did not recover, and was not included in the analysis (Fig. 3b). Cup wear rates over 10-million cycles appeared very stable with excellent consistency (Fig. 3c). By end of test, the edge-wearing cups averaged 3.7 times higher wear than mating heads. Overall MOM wear averaged 1.6mm³ per million cycles. Apart from the first 100,000 cycles of run-in, no lubricant changed color during entire test.

In this first study of its kind, we demonstrated both normal and edge-wear wear-patterns in accordance with predictions of the steep-cup algorithm (Clarke 2015), satisfying hypothesis #1. Wear rates with Inverted cups averaged 2.7 times greater wear than those in similar Anatomical study (Bowsher, 2009), satisfying hypothesis #2. The 60mm MOM wear rates Inverted were mid-range to those in the prior steep-cup Anatomical tests (range 1.3 – 1.9mm³ per 10⁶ cycles). This neither satisfied nor eliminated hypothesis #3, perhaps due to confounding effects, i.e. different designs, MOM diameters and methods. In conclusion, the Inverted test in the simulator appears to offer considerable merit, perhaps analogous to patients who experience edge-wear only intermittently. In contrast the Anatomical test mode appears analogous to patients with mal-positioned cups, who therefore walk on the cup rim constantly throughout their gait cycle.

Introduction

Over 40-years the dominant form of implant fixation has been bone cement (PMMA). However the presence of circulating PMMA debris represents a 3rd-body wear mechanism for metal-on-polyethylene (MPE). Wear studies using PMMA slurries represent tests of clinical relevance (Table 1). Cup designs now use many varieties of highly-crosslinked polyethylene (HXPE) of improved wear resistance. However there appears to be no adverse wear studies of vitamin-E blended cups.1–4 The addition of vitamin E as an anti-oxidant is the currently preferred method to preserve mechanical properties and ageing resistance of HXPE. Therefore the present study examined the response of vitamin-E blended liners to PMMA abrasion combined with CoCr and ceramic heads. The hip simulator wear study was run in two phases to compare wear with, (i) clean lubricants and (ii) PMMA slurries.

The relevance of fluid-film lubrication, elasto-hydrodynamic lubrication and ‘tribolayers’ for hip bearings has been the subject of much debate (Fisher 2012). However, knowledge of the thickness and distribution of proteins in and around the wear zone of metal-on-polyethylene (MPE) bearings is scant. The efficacy of protein lubrication with metal-on-metal bearings (MOM) is in discovery. This simulator study was designed to analyze film formation on MOM bearings using varied protein concentrations. The hypotheses were that increasing protein concentrations in the serum lubricant would result in 1) greater thickness of protein films, and 2) reduced MOM wear.

The hip simulator was run for 5 million cycles (5 Mc) duration using 28 mm MOM bearings (DJO Inc) run with the cups anatomical. Lubricant protein concentrations were 16.5, 33, and 66 mg/ml. At each test interval of 1 Mc, the proteins films on CoCr surfaces were analyzed by both interferometry and SEM imaging in main-wear, transition-wear and non-wear zones. Thickness of protein films was measured using non-contacting interferometry. Areas of wear zones were mapped and measured and the areas compared. MOM wear rates were assessed gravimetrically.

It was found that the proteins formed two types of film (Figure 1). Type-1 was visually hazy in appearance, grainy in structure, and most commonly found in the main-wear zone. This type of protein film was always present in the main-wear zone but its thickness (approximately 0.05 μm) did not increase with increase in the lubricant protein concentrations. Type-2 was visually rainbow-like in appearance, more gel-like with thick clumps appearing as islands on the CoCr surfaces, and more common in the transition zone. This type of film was always present (approximately 1 μm thick) and its thickness notably increased in cups with increased lubricant protein concentrations. This film remained relatively consistent on femoral heads and did not change with increased protein concentrations (Figure 2).

The type-1 protein films were always detectable in the actual wear zones but only the type-2 film showed a build-up with protein concentration and only inside the cups. This may be partially a response to the orbital simulator set up. In the Anatomical test mode, the cup is fixed with respect to the load axis and the head oscillates. Thus the main-wear zone on the head had a distributed type of wear patch and the main-wear zone in the cup was fixed. This configuration would allow the type-2 proteins to accumulate around the edge of the cup wear zone. In contrast, they would be scraped off the wear zone of the orbiting femoral head. This study showed that protein films endure even inside the main-wear zone of MOM bearings. In addition, collaborative studies have shown that the protein films are highly mobile and stream across the main-wear zones. Thus there is both an interaction with the CoCr surfaces and a degradation phenomenon that likely results in the protein-rich layers in the transition regions.

Figure 1: SEM images of type 1 and type 2 protein films.

Figure 2: Protein films on MOM bearings under three different protein concentrations.

Is is believed that 3rd-body wear of polyethylene, be it from particles of bone, bone-cement (PMMA), or metal, is an unavoidable risk in total hip arthroplasty (THA). Simulator studies have demonstrated that wear in conventional polyethylene (CXPE) and highly crosslinked polyethylene (HXPE) cups increased 6 and 20-fold respectively when challenged by circulating 3^rd-body PMMA particulates. There was no corresponding change in head roughness, i.e. the PMMA did not roughen CoCr surfaces. Many contemporary cup designs now use the vitamin-E process combined with higher crosslinking dosage (VEPE). However, little if anything is known about the VEPE debris. Therefore in this study we analyzed the morphology of VEPE particles from cups that had been run in, a) standard simulator test mode and b) adverse PMMA debris-challenge mode. The aim of this study was to determine how a clinically relevant challenge, such as addition of PMMA particles affected the wear debris. This had not been attempted previously due to contamination polyethylene by PMMA debris. The hypotheses were that, a) during the ‘clean’ test, VEPE would yield smaller debris of standard globular shape compared to controls (XPE) and b) in adverse PMMA challenge mode, VEPE debris size would increase and become more flake-like.

The XPE and vitamin-E blended cups (VEPE) cups were gamma-irradiated at 7.5 Mrad and 15 Mrad, respectively. Cups were run Inverted and mated with ceramic femoral heads of diameter 44 mm (Biolox-delta, Ceramtec). The three test phases included; ‘clean’ for 6 million cycles (6 Mc), abrasive slurry 6–8 Mc (concentration 10g/L), and ‘clean’ 8–10 Mc. The debris was isolated using standard procedure for ‘clean’ tests and a modified procedure for the abrasive slurries. Particles were imaged using SEM and the micrographs analyzed (Image J). Approximately 600 particles were analyzed from each sample (4.5 Mc and 8 Mc) and morphology defined via aspect ratio (AR), equivalent circular diameter (ECD), and circular shape factor (CSF).

The clean test revealed slight differences in shape factors for XPE and VEPE (AR, CSF within 30%: p <0.0001) but none with regard to size (p > 0.9999). The median ECD for both XPE and VEPE was approximately 0.55 μm. The abrasive test revealed a statistical difference (p < 0.0001) in shape compared to the clean test, but varied less than 25%. The greater change in debris morphology between the abrasive test and clean test was size, which increased 3.6 fold for VEPE particles (ECD = 2.0 μm) and 4.3 fold for XPE particles (ECD = 2.3 μm).

It was determined that addition of vitamin E to the PE did not change the size, but did change the shape of PE debris particles up to 30%. This study was the first to isolate debris particles during an abrasive slurry test and determine morphology under such conditions. Debris particles formed in abrasive conditions were found to be 4-fold larger in diameter, suggesting a larger volume of shreds in comparison to the mostly submicron population observed under standard testing conditions.

Figure 1: Boxplot of equivalent circular diameter values.

Figure 2: Boxplot of aspect ratio values.

Figure 3: Boxplot of circular shape factor values.

Damage to metal-on-metal bearings (MOM) has been varyingly described as “edge wear,” third-body abrasive wear and “rim-damage” (1–4). However, no distinction has been made between any of these proposed wear mechanisms. The goal of this study was to discover what features might differentiate between surface damage created by either 2-body or 3-body wear mechanisms in MOM bearings. The hypotheses were that surface damage created by impingement of the cup rim (2-body wear) would be i) linear on the micro-scale, ii) reveal transverse striations (in direction of the sliding rim), iii) have either no raised lip or have a single lip along one side of the track, and iv) have an asymmetrical surface profile across the track width.

Five cases with 28 mm MOM, five of 34–38 mm MOM, and five of 50–56 mm diameter were studied (N = 15). The main wear zone (MWZ) was measured in each MOM head and the number of 2-body wear tracks recorded in the non-wear (NWZ) and main wear zone (MWZ). Bearing damage was examined using a white-light interferometer (Zygo Newview 600; 5x lens) and a scanning electron microscope (Zeiss MA15). The depths and slopes were assessed across the width of the damage tracks.

Thirteen of the 15 MOM bearings showed wear tracks that exhibited all four of the hypothesized 2-body wear characteristics. These wear tracks will be referred to as “micro-segments”. While micro-segments visually appeared linear, microscopically they revealed a semi-lunar edge coupled with transverse striations leading to a linear edge. This indicated that during impingement episodes, the cup rim ploughed material from the CoCr surface at the semi-lunar edge (Fig. 1), thereby creating the abruptly raised lip on the linear edge of the track. This “snow plough effect” and its distinct edge effect can account for the asymmetrical surface profile. A different type of 2-body wear was identified and referred to as “furrows”. Furrows also visually appeared linear visually, but microscopically revealed longitudinal striations and a symmetrical surface profile (Fig. 2). Furrows had lips raised on both sides of the track, but not circumscribing the terminal ends of the track. Instead, the ends of the furrows are tapered smooth transitions to the articular surface.

Thus, 2-body tracks were found to be distinguishable from 3-body tracks (micro-grooves) and were classified as either micro-segments or furrows. Micro-segements supported hypotheses 1–3 and provided a clearer definition for hypothesis-4, while furrows only supported hypothesis 1. The divergence in features between micro-segments and furrows allude to different interactions between the bearing and cup rim that led to each type of track. While these data represent a small set of cases (n = 15) this evidence shows for the first time what was previously only suspected (2), that the CoCr rim can routinely create 2-body wear damage mechanisms in MOM femoral heads.

Controversy has existed for decades over the role of fretting-corrosion in modular CoCr heads used with stems of CoCr vs Ti6Al4V. Since retrieval data on taper performance remains scant, we report here an18-year survivorship of a Ti6Al4V: CoCr combination (APR design; Intermedics Inc). Unique to this study were the threaded profiles present on both stem and head tapers (Fig. 1).

This female patient was revised for pain, osteolysis and recurrent hip dislocation at 17 years, 10 months. A prior MPE hip replacement performed for her severely dysplastic right hip had lasted 11 years. At this 2nd revision, the 28 mm CoCr head was found dislocated posteriorly and superiorly. Metallosis was evident in the tissues. The polyethylene liner showed extensive rim damage on both anterior and posterior aspects. The neck of her APR Revision stem (Intermedics Inc) had worn through the polyethylene rim and impinged on the metal cage. The cage was found loose, the liner had disassociated, and the peri-trochanteric areas were compromised by massive osteolysis. The femoral stem and head were removed together without disassembly. The femoral stem and acetabular construct were replaced by an ARCOS revision system using 36 mm head with a Freedom cup (cemented to Max-Ti cage; Biomet Inc.).

The complete femoral neck and head were bi-valved assembled in horizontal plane for direct imaging by interferometry and SEM (Fig. 1a). After sectioning the head separated from the stem. Quantitative imaging used 1 to 5 regions with 6-replicate measurements per region and differentiation into contact and non-contact zones (Fig. 1b). Visual corrosion mapping (3) was recorded digitally in 4 anatomical views (Figs 1b–f).

The thread profile on contact zone inside the head (Fig. 2a) had a pitch of approximately 40 μm and a peak-to-valley depth of 4 μm overall (Fig. 2b profile section of thread: PV = 2 μm). The thread profile on stem trunnion (Fig. 3a) had a pitch of approximately 125 μm and a peak-to-valley depth of 3.5 μm overall (Fig. 2b profile section of thread: PV = 1 μm). Thus the stem trunnion thread was much coarser than the head. Overall corrosion grading was judged very mild. Overall we were satisfied that this Ti6Al4V: CoCr combination taper junction with threaded interfaces had performed very well for 18 years. Nevertheless, our visual grading was subject to opinion and thus unrewarding. The continuing project will quantify the contacting and non-contacting regions of head and stem (Fig. 1b).

It has come to light that one significant mechanism for MOM failure may be repeated subluxation or impingement episodes leading to edge wear and release of 3^rd body particles. This MOM debris-challenge model simulates a patient who experienced one subluxation or impingement event and then continues to walk normally until the next event occurs one week later. Our model assumes that 100–200 particles (debris size 100–200 μm) would be released into the joint space at each subluxation or impingement event. The question then becomes: what is the effect of the patient walking on that single dose of particulates over the next week (or 500,000 cycles in simulator test mode).

Nine 38 mm CoCrMo bearings (DJO Inc., Texas) were run inverted in a12-station hip simulator (SWM, Monrovia, CA). The test was run in standard simulator mode (Paul gait load cycle: 0.2–2 kN, frequency 1 Hz) with the addition of 5 mg of debris particles for the first 3 Mc, followed by 10 mg of debris particles from 3–5 Mc. Commercially available CoCr (ASTM F75) and titanium alloy (ASTM F136) particles and broken polymerized bone cement particles were used in the size range 50–200 μm. Serum was changed out every 500,000 cycles and a fresh dose of debris added. All bearings were ultrasonically cleaned and examined using white light interferometry (WLI, Zygo Corp) and SEM (EVO MA15, Zeiss). Wear rates were determined gravimetrically and serum discoloration was noted at each test interval.

Titanium alloy and CoCr debris produced darkened serum within the first hour of the test and remained so for the duration (500,000 cycles). Serum color with cement debris remained an opaque golden color throughout the test run. The debris challenge provoked the largest MOM wear response using Ti6Al4V particulates (6.7 mm³/Mc), slightly milder with CoCr particulates (4.5 mm³/Mc) and minimal with PMMA particulates (0.5 mm³/Mc). Compared to bone cement debris chambers (which had wear rates comparable to non abrasive MOM bearing tests), CoCr debris created a 9-fold higher MOM wear and titanium alloy debris created a 14-fold higher MOM wear. These observations indicated that only the metal debris elicited an ‘Adverse’ wear response with MOM bearings.

There is a consensus that impingement, subluxation, and dislocation are major risks that can lead to failure in total hip arthroplasty (1). As well as producing edge-wear, such clinical events also may create additional loads of particulate debris (2). It has been suggested that the release of metal debris with collateral damage on metal-on-metal (MOM) bearings creates a particularly severe abrasive wear, hitherto not understood, and recently termed ‘micro-grooving’ (3,4). Perhaps related to this micro-grooving, large surface depressions have also been observed. These we labeled ‘Dongas’, from the South African term for a steep-sided gully created by erosion. The goal of this study was to examine Dongas found on retrieved MOM bearings and to correlate factors such as cause of revision, MOM diameter and Donga locations with respect to regions of normal and stripe wear. Our hypotheses were: (1) Dongas will be most visible in non-wear zones (NWZ) adjacent to the main-wear zone boundary (MWZ), (2) the 28 mm MOM, being inherently less stable compared to large-diameter MOM, will show a higher Donga frequency and (3) patients with subluxation or dislocation complaints will reveal a higher Donga frequency.

Five cases with 28 mm MOM, five of 34–38 mm, and five of 50–56 mm diameter were studied (N = 15). The MWZ was measured in each MOM head and the number of NWZ and MWZ Dongas recorded. Bearing damage was examined using a white-light interferometer (Zygo; 5x lens).

Dongas were mainly elliptical in shape, but sometimes highly irregular. They were commonly circumscribed by raised lips (Fig. 1). Donga “trails” were also found, appearing as a linear series of similar-sized Dongas (Fig. 2). Donga trails exhibited some variability with raised lips either lining only the opposite sides or circumscribing most of the perimeter. The Dongas were commonly found in NWZ, with less than 20% found in MWZ. For this set of 15 MOM bearings, large-diameter bearings showed the largest number of Dongas and the greatest frequency of Dongas resulted from either loose or migrating cups.

The high occurrence of dongas in the non-wear zone (supporting hypothesis-1) may be a result of particles swept into the bearing interface (2,5). The size of the Dongas and their frequent association to local micro-grooves indicated that these were the impact sites of circulating particles. Such large surface depressions (40–200 μm) have not been described previously and may be unique to MOM bearings (3,4). The observation that Dongas were most prevalent in cases with loose or migrating cups left hypothesis-2 unsatisfied. The much higher incidence of Dongas in the large-diameter MOM was surprising and negated hypothesis-3. Overall these new data relating Dongas and micro-grooves gives new credence to a hitherto unsuspected 3^rd-body abrasive wear mechanism due to repetitive subluxation or impingement.

The MOM controversy continues with many prevailing opinions as to the causes of failure in contemporary designs. There has been a great deal of focus on breakdown in fluid-film lubrication with respect to cup positioning and edge wear at its rim. However there has been very little discussion on the problems of 3^rd body abrasion. In only one study was there a description of unusually large abrasive marks on retrieved femoral heads (McKee Farrar MOM), revealing 100 μm wide scratches, attributed to circulating particles fractured during impingement episodes. With contemporary MOM devices, there is the potential for abrasion by particulates of CoCr, PMMA and Ti6Al4V. However it has been difficult to formulate a coherent simulator model for 3^rd-body abrasive wear, given the unpredictable nature of impingement damage releasing abrasive particles into the patient's hip joint. Thus this study sought to identify if metal or cement particulates were capable of creating 100 μm wide scratches as seen on retrieved MOM and develop a simulator model for 3^rd body abrasive testing on MOM bearings.

Six 38 mm CoCrMo bearings (DJO Inc., Texas) were run in a12-station hip simulator (SWM, Monrovia, CA) with cups mounted both anatomically and inverted (3 MOM each). The tests were run in standard simulator mode (Paul gait load cycle: 0.2–2 kN, frequency 1 Hz) with the addition of 5 mg of debris particles. Commercially available CoCr (ASTM F75) and titanium alloy (ASTM F136) particles and broken polymerized bone cement particles were used in the size range 50–200 μm. The simulator was run for only 10 cycles and the MOM parts removed for study. All bearings were ultrasonically cleaned and heads were examined using white light interferometry (WLI, Zygo Corp). Grooves were characterized using surface profiles to measure width, depth, and rim height. SEM imaging (EVO MA15, Zeiss) and EDS imaging (X flash detector 4010, Bruker AXS) was performed in areas of grooving and suspected transfer layers.

CoCr debris produced broad, curvilinear grooves with widths ranging from 20–170 μm, depths from 0.3–1.5 μm, raised rims, longitudinal striations and chatter marks. Titanium alloy debris produced arrays of very shallow scratches accompanying larger grooves. These larger grooves measured 20–110 μm wide and 0.4–1.9 μm deep.

EDS imaging showed the smears and islands contained the elements Ti, Al and V representative of the Ti6Al4V alloy. WLI imaging showed these metal deposits (250–900 um wide) were raised >10 um above the surface. Particularly conspicuous was evidence of considerable smearing on CoCr surfaces, with linear streaks ranging 150–300 μm wide. Bone cement debris proved incapable of grooving the CoCr surface, the only scratches observed were those comparable to normal carbide scratches.